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CRYOGENIC TWO-PHASE FLOW DURING CHILLDOWN: FLOW TRANSITION
AND NUCLEATE BOILING HEAT TRANSFER
By
JELLIFFE KEVIN JACKSON
A DISSERTATION PRESENTED TO THE GRADUATE SCHOOL OF THE UNIVERSITY OF FLORIDA IN PARTIAL FULFILLMENT
OF THE REQUIREMENTS FOR THE DEGREE OF DOCTOR OF PHILOSOPHY
UNIVERSITY OF FLORIDA
2006
This work is dedicated to my parents, Victor and Eva Jackson. Without their continuous support and encouragement this work would not have been possible.
iv
ACKNOWLEDGMENTS
The author would like to express his sincerest gratitude to his academic advisor and
PhD committee chairperson, Professor James Frederick Klausner. His guidance, support,
encouragement and insight contributed immensely to the accomplishment of this work.
The author would also like to express his appreciation to Professor Renwei Mei for his
invaluable input, which helped to guide this work through times when the path was
cloudy. The author would like to thank Professor David Hahn, Professor William Lear
and Professor Samim Anghaie for serving on his PhD committee. Their insight has
helped the author to develop the necessary critical thinking skill needed to become a
contributing member of the academic community.
The assistance, encourage and friendship provided by the author’s fellow research
associates are greatly appreciated. The technical assistance provide by Mr. Christopher
Velat, in the construction phase of the experimental facility is also greatly appreciated.
This research was supported by the National Aeronautics and Space Administration
Glenn Research Center, through contract NAG3-270. Without its financial support this
work would not be possible.
Most importantly, the author wishes to express his deepest gratitude and
appreciation to his wife, Aisha Ivette Wood-Jackson, for her unwavering support and
patience throughout the course of this endeavor. She has provided the much needed
encouragement in times when self-doubt was creeping into the author’s mind and she
v
continues to be a source of comfort and inspiration. Without her support, encouragement
and patience, this work would not have been possible.
vi
TABLE OF CONTENTS page
ACKNOWLEDGMENTS ................................................................................................. iv
LIST OF TABLES........................................................................................................... viii
LIST OF FIGURES ........................................................................................................... ix
NOMENCLATURE ........................................................................................................ xiv
ABSTRACT..................................................................................................................... xix
CHAPTER
1 INTRODUCTION ........................................................................................................1
2 LITERATURE SURVEY.............................................................................................6
Horizontal Flow Regimes .............................................................................................6 Flow Regime Maps for Horizontal Flow......................................................................8
The Baker Map ......................................................................................................8 The Taitel and Dukler Map ...................................................................................9 The Steiner Map ..................................................................................................13 The Wojtan et al. Map .........................................................................................14
Forced Convection Boiling Heat Transfer Correlations.............................................16
3 EXPERIMENTAL FACILITY ..................................................................................31
System Overview........................................................................................................31 Visual Test Section Design.........................................................................................33 Instrumentation and Calibration .................................................................................34
Static Pressure Transducers.................................................................................34 Test Section Pressure Drop .................................................................................34 Flow Meter Calibration .......................................................................................35 Temperature Measurements ................................................................................36
Data Acquisition System ............................................................................................38 Digital Imaging System ..............................................................................................39 Experimental Protocol ................................................................................................40
vii
4 DATA PROCESSING................................................................................................41
Vapor Quality Estimation ...........................................................................................41 Vapor Volume Fraction ..............................................................................................43 Extracting the Heat Transfer Coefficient....................................................................44
Computing the Temperature Field in the Pipe Wall............................................46 Iteration Process for Guessing the Inner Heat Transfer Coefficient ...................50 Test for Convergence ..........................................................................................50
Computational Code: Testing and Verification..........................................................51 Stability of Computational Code .........................................................................51 Grid Resolution ...................................................................................................51
Testing the Inverse Procedure ....................................................................................52
5 CHILLDOWN FLOW TRANSITION AND HEAT TRANSFER............................57
Flow Regimes .............................................................................................................62 Experimental Observations .................................................................................64 Performance of Current Flow Regime Maps.......................................................65 Calibration of Taitel and Dukler Flow Regime Map...........................................68
Film Boiling Heat Transfer.........................................................................................75 Nucleate Flow Boiling Heat Transfer.........................................................................76
Performance of Current Flow Boiling Heat Transfer Correlations .....................78 Correlating the Nucleate Flow Boiling Heat Transfer Coefficient......................82
6 CONCLUSIONS AND RECOMMENDATIONS FOR FUTURE RESEARCH......98
APPENDIX
A PHYSICAL PROPERTIES OF NITROGEN...........................................................101
B EXPERIMENTAL DATABASE: FLOW REGIME, HEAT TRANSFER COEFFICIENT, AND PRESSURE DROP DURING CHILLDOWN....................103
LIST OF REFERENCES.................................................................................................174
BIOGRAPHICAL SKETCH ...........................................................................................180
viii
LIST OF TABLES
Table page 2-1 Empirical constants for the Kandlikar correlation. ..................................................25
4-1 Influence of grid resolution on the computed outer wall temperature .....................52
5-1 Sample data points for cryogenic chilldown. SW denotes stratified-wavy flow; I denotes intermittent flow; A denotes annular flow ..................................................70
5-3 Summary of measured average nucleate flow boiling heat transfer coefficients using inverse method for regions. ............................................................................81
ix
LIST OF FIGURES
Figure page 2-1 Schematic representation of flow regimes observed in horizontal two-phase
flow.............................................................................................................................7
2-2 The Baker flow regime map.....................................................................................10
2-3 The Taitel and Dukler flow regime map. .................................................................13
2-4 The Steiner flow regime map. ..................................................................................14
2-5 The Wojtan et al. flow regime map..........................................................................15
2-6 Flow structures used to evaluate stratified flow liquid film thickness and stratified angle. .........................................................................................................28
2-7 Flow structures used to evaluate (a) annular flow liquid film thickness, (b) annular flow liquid film thickness and partial-dry out angle ...................................29
3-1 Schematic of chilldown experimental facility..........................................................31
3-2 Schematic of the flange assembly. ...........................................................................33
3-3 Calibration plot of the actual velocity versus the ideal velocity (Velat [56]). .........36
3-4 Thermocouple arrangement on the steel transfer line prior to the visual test section.......................................................................................................................37
3-5 Thermocouple placement for heat transfer test section............................................38
4-1 Model used for the stratified, wavy and intermittent flow volume fraction computation. .............................................................................................................44
4-2 Diagram of the model used for the annular flow volume fraction computation. .....44
4-3 Flow chart for transient heat transfer coefficient extraction. ...................................45
4-4 Coordinate system for heat conduction through the pipe wall.................................47
4-5 Calibration for determining the outer pipe surface heat transfer coefficient. ..........48
x
4-6 Assumed variation of heat transfer coefficient on the inside surface of the pipe. ...50
4-7 Computation of a parabolic varying heat transfer coefficient using the inverse method. .....................................................................................................................55
4-8 Comparison of heat transfer coefficient computed using the inverse procedure and the Dittus-Boelter correlation for single-phase nitrogen gas flow. ...................56
5-1 Quenching front that marks transition for film boiling to nucleate boiling .............57
5-2 Temperature profile during chilldown for low mass flux experiment. ....................58
5-3 Temperature profile during chilldown for moderate mass flux experiment. ...........59
5-4 Transient mass flux for low mass flux experiment. .................................................59
5-5 Transient mass flux for moderate mass flux experiment. ........................................60
5-6 Transient vapor volume for low mass flux experiment............................................60
5-7 Transient vapor volume fraction for moderate mass flux experiment. ....................61
5-8 Transient vapor quality for low mass flux experiment. ...........................................61
5-9 Transient vapor quality for moderate mass flux experiment....................................62
5-10 Transient inlet pressure profile for low mass flux experiment.................................63
5-11 Transient inlet pressure profile for moderate mass flux experiment........................63
5-12 Comparison of Van Dresar and Siegwarth data with the Baker map.......................67
5-13 Comparison of Van Dresar and Siegwarth data with the Taitel and Dukler map. ...67
5-14 Comparison of Van Dresar and Siegwarth data with the Wojtan et al. map............68
5-15 Comparison of current chilldown data with the Baker map.....................................69
5-16 Comparison of current chilldown data with the Taitel and Dukler map. .................69
5-17 Comparison of current chilldown data with the Wojtan et al. map..........................71
5-18 Liquid-vapor 2-D channel flow configuration. ........................................................72
5-19 Comparison of current chilldown data with the modified Taitel and Dukler map. .75
5-20 Heat transfer coefficients for each region in the film boiling regime of the low mass flux experiment. ..............................................................................................77
xi
5-21 Heat transfer coefficients for each region in the film boiling regime of the moderate mass flux experiment................................................................................77
5-22 Average two-phase heat transfer coefficient variation with time.............................79
5-23 Comparison of predicted and measured average nucleate flow boiling heat transfer coefficients using Gungor and Winterton correlation.................................83
5-24 Comparison of predicted and measured average nucleate flow boiling heat transfer coefficients using Kandlikar correlation. ....................................................83
5-25 Comparison of predicted and measured average nucleate flow boiling heat transfer coefficients using Müller-Steinhagen correlation. ......................................84
5-26 Comparison of predicted and measured average nucleate flow boiling heat transfer coefficients using Wojtan et al correlation. ................................................84
5-27 Method for assigning the heat transfer coefficient on the inside surface of the pipe. ..........................................................................................................................85
5-28 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................87
5-29 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................87
5-30 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................88
5-31 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................88
5-32 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................89
5-33 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................89
5-34 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................90
5-35 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................90
5-36 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................91
5-37 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................91
xii
5-38 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................92
5-39 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................92
5-40 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................93
5-41 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................93
5-42 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................94
5-43 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................94
5-44 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................95
5-45 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................95
5-46 Comparison of the predicted and measured temperatures using both the Müller-Steinhagen and Jamialahmadi correlation and the modified version.......................96
5-47 Comparison of predicted and measured average nucleate flow boiling heat transfer coefficients using modified Müller-Steinhagen correlation........................97
xiv
NOMENCLATURE
A cross-sectional area (m2)
a constant in the Müller-Steinhagen and Jamialahmadi correlation
Bo Boiling number
0C empirical constant in Zuber Findlay correlation
1 5C C− constants in the Kandlikar correlation
2C coefficient dependent on the size of disturbance
Co Convection number
c interface wave speed (m/s)
pc specific heat capacity (J/kgK)
D inner diameter of pipe (m)
d pipe wall thickness (m)
E enhancement factor
F modified Froude number
kF fluid property enhancement factor for nucleate boiling in the
Kandlikar correlation
pF pressure function
Fr Froude number
G mass flux (kg/m2s)
g gravitational acceleration (m/s2)
xv
h heat transfer coefficient (W/m2K)
fgh latent heat of vaporization (J/kg)
K wavy flow dimensionless parameter
k thermal conductivity (W/mK)
M molecular weight
Ma Mach number
m wave number
n exponent
P pressure (Pa)
Pr Prandtl number
q′′ heat flux (W/m2)
R inner radius of pipe (m)
Re Reynolds number
pR surface roughness (m)
r radial coordinate
S suppression factor also slip velocity (m/s)
1S modified suppression factor
s shelter coefficient
T dispersed bubble floe dimensionless parameter also temperature
(K)
t time (s)
vjU empirical constant in Zuber-Findlay correlation
xvi
u fluid velocity (m/s)
V voltage output (V)
ttX Martinelli parameter
x vapor quality
Y parameter encompassing relative forces acting on the fluid due to
Gravity and pressure
z axial coordinate
Greek Symbols
α vapor void fraction
δ fluid film height (m)
ε scaling factor
Φ annular correction factor
φ azimuthal coordinate
γ angle of inclination of pipe (rad.) also ratio of specific heats
ϕ dimensionless temperature
λ fluid property correction factor for vapor mass flux in the Baker
map
µ fluid viscosity (Pa-s)
ν kinematic viscosity (m2/s)
θ angle film occupies (rad.)
ρ density (kg/m3)
σ surface tension (N/m)
sΨ enhancement factor of Shah
xvii
ψ fluid property correction factor for liquid mass flux in the Baker
Map
Subscripts
0 denotes reference quantity
1t denotes single-phase
2φ denotes two-phase quantity
∞ denotes far field condition
a denotes air
actual denotes actual quantity
b denotes nucleate boiling
bottom denotes bottom of the pipe
c denotes single-phase convection
crit denotes critical quantity
dry denotes dry perimeter of pipe
fl denotes fluid inside pipe
fo denotes liquid only
g denotes vapor phase
i denotes liquid vapor interface
ib denotes point of incipient boiling
ideal denotes ideal quantity
in denotes inner surface of the pipe
known denotes known quantity
l denotes liquid phase
xviii
new denotes new quantity
ONB denotes onset of nucleate boiling
out denotes outer surface of pipe
pres denotes present quantity
prev denotes previous quantity
r denotes reduce
sat denotes saturation condition
side denotes side of the pipe
top denotes top of the pipe
w denotes quantity is evaluated at the pipe inner wall
wa denotes water
wet denotes wetted area of inner pipe wall
Superscripts
s denotes superficial quantity
~ denotes dimensionless quantity
xix
Abstract of Dissertation Presented to the Graduate School of the University of Florida in Partial Fulfillment of the Requirements for the Degree of Doctor of Philosophy
CRYOGENIC TWO-PHASE FLOW DURING CHILLDOWN: FLOW TRANSITION AND NUCLEATE BOILING HEAT TRANSFER
By
Jelliffe Kevin Jackson
August 2006
Chair: James F. Klausner Major Department: Mechanical and Aerospace Engineering
The recent interest in space exploration has placed a renewed focus on rocket
propulsion technology. Cryogenic propellants are the preferred fuel for rocket propulsion
since they are more energetic and environmentally friendly compared with other storable
fuels. Voracious evaporation occurs while transferring these fluids through a pipeline that
is initially in thermal equilibrium with the environment. This phenomenon is referred to
as line chilldown. Large temperature differences, rapid transients, pressure fluctuations
and the transition from the film boiling to the nucleate boiling regime characterize the
chilldown process.
Although the existence of the chilldown phenomenon has been known for decades,
the process is not well understood. Attempts have been made to model the chilldown
process; however the results have been fair at best. A major shortcoming of these models
is the use of correlations that were developed for steady, non-cryogenic flows. The
xx
development of reliable correlations for cryogenic chilldown has been hindered by the
lack of experimental data.
An experimental facility was constructed that allows the flow structure, the
temperature history and the pressure history to be recorded during the line chilldown
process. The temperature history is then utilized in conjunction with an inverse heat
conduction procedure that was developed, which allows the unsteady heat transfer
coefficient on the interior of the pipe wall to be extracted.
This database is used to evaluate present predictive models and correlations for
flow regime transition and nucleate boiling heat transfer. It is found that by calibrating
the transition between the stratified-wavy and the intermittent/annular regimes of the
Taitel and Dukler flow regime map, satisfactory predictions are obtained. It is also found
that by utilizing a simple model that includes the effect of flow structure and
incorporating the enhancement provided by the local heat flux, significant improvement
in the predictive capabilities of the Müller-Steinhagen and Jamialahmadi correlation for
nucleate flow boiling is achieved.
1
CHAPTER 1 INTRODUCTION
Cryogenic fluids have been used in various applications over the past century. One
application that has continuously been getting attention has been the use of cryogenic
propellants for rocket propulsion. This interest has been sparked by the fact that
cryogenic propellants yield more energy and are more environmentally friendly, when
compared to non-cryogenic propellants [1] and the storage systems for these cryogenic
propellants are lighter than those required for their non-cryogenic counterparts [1].
Before these propellants can be used for propulsion in space they must first be filled in
their respective storage containers while still on the ground. The introduction of the
cryogenic fluid in a transfer line that is in thermal equilibrium with environment results in
voracious boiling within the line; this phenomenon is referred to as line “chilldown” or
line “cool-down”. Chilldown is characterized by large temperature differences, rapid
transients and pressure fluctuations.
The phenomenon of chilldown is of interest since it directly impacts the design of
the delivery system for the propellant. For example the magnitude of the pressure
oscillations determines the thickness of the material used for the transfer lines, and the
heat transfer rate determines the type and thickness of insulation to be used. Other
important factors that must be considered when dealing with chilldown are the quantity
of liquid propellant vaporized, the time it takes for the transfer line to be completely
cooled, and the degree to which bowing of the transfer lines occur, especially during the
instances where the flow is in the stratified regime. Hence a proper understanding of the
2
chilldown process would allow for more economical and robust designs of cryogenic
propellant delivery systems.
Over the past few decades attempts have been made to understand this complex
process through experiments and numerical simulations. In 1960 Burke et al. [2] applied
the principle of conservation of energy and conservation of mass to the entire transfer
line, and as result he developed a simple model to estimate chilldown time. The model
showed reasonable agreement with their experimental results; however the overall
accuracy is limited due to broad assumptions, averaging of fluid properties and averaging
of mass flow rates. The experiments performed demonstrated the unsteady and
oscillatory nature of the chilldown process.
Two years after the study of Burke et al., Bronson et al. [3] performed experiments
of their own, where they evaluated the model of Burke for chilldown time and a model
for estimating the frequency of pressure oscillations. It was determined that these models
gave an acceptable prediction of chilldown time. Bronson et al. were able to highlight
the existence of circumferential temperature variations.
Steward, Smith and Brennan [4] carried out the first detailed numerical simulation
of the process in 1970. They were able to utilize the computational technology available
at the time to solve the continuity, momentum and energy equations. With the aid of
numerous assumptions, they were able to investigate pressure variations, estimate
chilldown time and predict temperature profiles. It was concluded that pressure surges
are exacerbated by a high degrees of subcooling of the inlet fluid, long transfer lines,
dense fluids and rapid opening of the inlet valve.
3
In the mid 1970’s a series of studies [5-7] on the cool-down of short transfer lines
were performed. These studies utilized an energy balance for an elemental length of pipe
to determine the temperature of the pipe wall as a function as time. The flow structure
and the momentum transport were neglected in the analysis, and heat transfer coefficient
correlations utilized were those developed for steady, non-cryogenic systems. Thus there
was poor agreement between the results of their analytical model and the experimental
data.
With the rapid advancement of computing technology during the past two decades,
more sophisticated numerical simulations of the chilldown process were attempted.
Papadimitriou and Skorek [8] developed a thermohydraulic code for the calculation of
system variables for both steady state and transient processes for two-phase cryogenic
flows. They utilized the conservation equations for both the liquid and vapor phases
coupled with various correlations for heat transfer coefficient and pressure drop, none of
which were developed for unsteady flow or cryogenic fluids. They were able to predict
the temperature and pressure history of the cooldown process; however their predicted
results consistently under-predicted the temperature and pressure.
In 2002 Cross et al. [9] developed a numerical procedure that utilizes the unsteady
conservation equations in conjunction with a thermodynamic equation of state and
correlations for boiling heat transfer. These correlations for boiling heat transfer were not
developed for two-phase cryogenic flows. They concluded that when the fluid enters the
transfer lines as a subcooled liquid 9.41 times the amount of fluid is consumed to achieve
chilldown as opposed to having the fluid enter as a superheated vapor.
4
The chilldown process is physically similar to the re-wetting phenomenon
encountered in the nuclear industry when re-establishing normal and safe temperature
levels following a loss of coolant accident (LOCA). In the event of a LOCA, the
temperature in the reactor core raises rapidly as a result of poor heat transfer due to the
dryout. In order to prevent catastrophic failure an emergency core cooling is done by
introducing a cooling fluid (usually water) into the reactor core. The cooling fluid is
several hundred degrees colder than the temperature of the reactor; thus voracious
evaporation takes place. The process proceeds in a similar manner to that of cryogenic
chilldown as it goes from the film boiling regime to the nucleate flow boiling regime and
eventually to the single phase convective heat transfer regime. Research in the area of re-
wetting usually focuses on the prediction of the quenching velocity [10-12]. Chan and
Banerjee [13-15] used a two-fluid numerical model to investigate the re-wetting and re-
filling in a horizontal tube and achieved reasonable agreement in the prediction of
quenching velocity. However the predictions of the temperature profile is not good
especially in the nucleate flow boiling regime, where it is observed that the discrepancy
in temperature is greater than 100 °C. This is a result of utilizing over simplified models
for the heat transfer coefficient.
It is evident from the previous studies on the chilldown process that the focus has
been on predicting chilldown time and simulating the flow so as to obtain the pressure
history, the temperature history and the fluid expenditure. However, all models to date
use empirical correlations for determining the heat transfer coefficient and the pressure
gradient that were developed steady non-cryogenic flows. The agreement with
experimental data has been fair at best.
5
Hence the purpose of this research investigation is to develop a database of flow
regime and heat transfer coefficient for cryogenic chilldown in horizontal transfer lines.
Techniques are also provided to predict flow regimes and nucleate flow boiling heat
transfer coefficients. This information will help practitioners develop more accurate and
reliable models, thus leading to more efficient and economical cryogenic delivery
systems. To carry out this study a horizontal once through chilldown facility utilizing
nitrogen as the working fluid was constructed. The facility allows for the flow structure
to be observed while simultaneously measuring and recording the mass flow rate,
temperature, and pressure within the test sections. At present, there is no database that
exists that includes a compilation of data for temperature, pressure, mass flow rate and
flow regimes that occur during chilldown. Hence the first step is to compile a large
database of temperature, pressure, mass flow rate and flow structure data for the
chilldown process. This database will be used to evaluate the heat transfer coefficients
that are experienced during chilldown, which will allow present predictive models and
correlations to be evaluated and calibrated for use in chilldown models.
A literature survey of flow structure and heat transfer predictions is given in the
next chapter. This is followed by a detailed description of the experimental facility in
chapter 3 that has been developed to compile the required database for cryogenic
chilldown. Chapter 4 describes the methods used to regress the experimental data and
extract the heat transfer coefficient. Chapter 5 compares the experimental data with
existing models or correlations and the modifications required to fit the data.
6
CHAPTER 2 LITERATURE SURVEY
In order to reliably predict the thermal transport associated with cryogenic
chilldown, it is important to know the flow structure and temperature variations. It is
useful to examine existing models for flow regime and heat transfer in two-phase flow.
The intent of this review is to examine the most widely employed predictive models and
examine their strengths and weaknesses, which allows the useful elements of the models
to be highlighted.
Horizontal Flow Regimes
During the chilldown process, the vapor and liquid are flowing simultaneously
inside the pipe. The resulting two-phase flow is more complex than single-phase flows.
Apart from the inertia, viscous, and pressure forces experienced in single-phase flow,
two-phase flows also experience interfacial tension forces, exchange of momentum,
mass and energy between the liquid and vapor phases, as well as the wetting
characteristics of the liquid on the pipe.
The flow structure that the two-phase flow evolves into is referred to as flow
regime and may take various forms depending on the flow rate of the various phases,
fluid property, and pipe geometry and orientation. The two-phase flow regimes that are
typically encountered for horizontal flow are illustrated in Fig. 2-1.
7
Figure 2-1. Schematic representation of flow regimes observed in horizontal two-phase
flow.
At very low vapor quality, bubbly flow is usually observed, with the bubbles
residing in the upper portion of the pipe (as a result of buoyancy forces). As the quality
is increased, the bubbles tend to coalesce producing larger plug-type bubbles, this is
referred to as plug flow. At low mass flow rates and higher qualities, stratified flow is
observed; as the flow rate and/or quality are increased the liquid-vapor interface becomes
unstable (due to Helmholtz instability), resulting in stratified-wavy flow. At high liquid
flow rates the amplitude of the waves may grow until the crest spans the cross-section of
the pipe forming large vapor slugs. This is referred to as slug flow. At higher vapor
velocities and moderate liquid flow rates the flow structure is observed to be annular,
with liquid film covering the entire circumference of the pipe with an inner vapor core. If
8
the vapor flow rate is very high and the vapor quality is also very high, it is possible for
the liquid to be entrained in the vapor forming what is known as mist flow.
Flow Regime Maps for Horizontal Flow
The prediction of the flow patterns existing in two-phase flows is essential for
developing phenomenological models for mass, momentum and energy transport within
those flow systems. Throughout the past decades numerous flow regime maps have been
developed for horizontal and vertical flows. Few maps have been developed
mechanistically [16, 17, and 18] as the vast majority of maps were developed through
empirical correlation methods [19, 20, and 21]. In this section the focus will be placed on
the most widely used maps for horizontal flow. An exhaustive review of all the existing
transition maps is not pursued here.
The Baker Map
The flow regime map proposed by Baker [19] in 1954 is one of the most widely
cited flow regime transition maps. This map was developed by an empirical correlation
method, which is comprised of plotting the observed flow pattern for air-water and
steam-water flows on a chart of liquid mass flux ( lG ) versus gas mass flux ( gG ). The
transition lines were then simply drawn onto the chart in such a manner as to divide the
area into regions associated with the flow pattern that was observed in that particular
area. In order to create maps for two-phase flow with fluids other than air-water and
steam-water, fluid property correction factors were introduced. Thus the coordinates of
the map are modified by the factors λ and ψ ,
21
⎥⎥⎦
⎤
⎢⎢⎣
⎡⎟⎟⎠
⎞⎜⎜⎝
⎛⎟⎟⎠
⎞⎜⎜⎝
⎛=
wa
l
a
g
ρρ
ρρ
λ (2.1)
9
31
2
⎥⎥⎦
⎤
⎢⎢⎣
⎡⎟⎟⎠
⎞⎜⎜⎝
⎛⎟⎟⎠
⎞⎜⎜⎝
⎛⎟⎠⎞
⎜⎝⎛=
l
wa
wa
lwa
ρρ
µµ
σσ
ψ (2.2)
where the subscripts g , l , a , and wa represent the gas, the liquid, air and water
respectively. ρ is the fluid density of the respective fluid, µ is the fluid viscosity of the
respective fluid, σ is the surface tension between the liquid and the gas and waσ is the
surface tension between water and air. The new coordinates of the map become lGψ
versus gGλ
.
This map has been used in studies involving cryogenic fluids [3, 22] with some
success. However this map has a severe shortcoming, which is the fact that the map
cannot take into account variations in pipe diameter or orientation. Variations in these
parameters were shown by Taitel and Dukler [16] to significantly affect the point at
which the transitions between flow regimes occur.
The Taitel and Dukler Map
The Taitel and Dukler [16] map, developed in 1976, is the first developed where
the transition mechanisms are based on physically sound concepts. The map was
developed with the assumption that the flow initially exists in the stratified regime and
subsequently transition into other regimes. Assuming the flow is initially stratified, a
momentum balance is carried out on each phase, and two non-dimensional groups were
uncovered that influence transition. These groups were defined as follows:
( )( )
2/
/
s
ltt s
g
dP dxX
dP dx= (2.3)
10
( )( )
sin
/l g
s
g
gY
dP dx
ρ ρ γ−= (2.4)
Figure 2-2. The Baker flow regime map.
where the subscripts l and g denote the liquid and gase phases respectively. ( )sdxdP /
is the pressure drop of one phase flowing within the pipe based on the mass fraction of
that phase, g is the gravitational acceleration and γ is the angle of inclination of the pipe
with respect to the horizontal. ttX is the Martinelli parameter and Y encompasses the
relative forces acting on the liquid due to gravity and pressure gradient.
11
The transition between stratified and intermittent or annular flow is modeled to take
place as a result of Helmholtz instability, which causes finite amplitude waves on the
surface of the stratified film to grow. The instability is a result of the Bernoulli effect, for
which the pressure is reduced as the gas accelerates over the crest of the wave. This
provides the basis for the following transition criterion,
2
2
/1 1G l l
g
u dA dhFC A
⎡ ⎤≥⎢ ⎥
⎢ ⎥⎣ ⎦ (2.5)
F is a Froude number modified by the density ratio,
( ) cos
sg g
l g
uF
Dgρ
ρ ρ γ=
− (2.6)
and the constant 2C is given by,
2 1 lCDδ
= − , (2.7)
where A is the flow cross-sectional area, δ is the film height, D is the diameter of the
pipe, u is the velocity of the respective phase, the superscript s denotes superficial for
single fluid flow, and the ~ indicates the quantity is dimensionless.
The transition to intermittent or annular flow is governed by the amount of liquid
available in the film. A transition to intermittent behavior occurs when the growing wave
encompasses enough of the liquid films so as to form a stable plug or slug. However if
there is not sufficient liquid in the film to develop a stable plug or slug, the flow assumes
an annular pattern. The amount of liquid that is sufficient to form intermittent flow is
seen to occur at a specific liquid film height, which is defined by a unique value of the
Martinelli parameter.
12
The transition between the stratified smooth and the stratified wavy patterns is
related to the wave generation phenomenon. In order for the stratified wavy pattern to
exist, the velocity of the gas must be sufficient to cause waves but not large enough to
cause rapid wave growth. It was hypothesized that this occurs when the pressure and
shear work on the wave is sufficient to overcome the viscous dissipation. The criterion
for transition from smooth to wavy flow is given by,
2
g l
Ku u s
≥ (2.8)
where s is the shelter coefficient defined in [16] and takes a value of 0.01 andK is the
product of the modified Froude number and the square root of the superficial Reynolds
number of the liquid:
( )( )
2
2 2 Re .cos
s sg gs l
lll g
u DuK FDg
ρ
νρ ρ γ
⎡ ⎤ ⎡ ⎤⎢ ⎥= = ⎢ ⎥⎢ ⎥− ⎣ ⎦⎣ ⎦ (2.9)
Here ν is the viscosity of the respective phase.
The transition between intermittent and dispersed bubble flow takes place when the
turbulent fluctuations are larger than the buoyancy force that keeps the gas at the top of
the pipe. This leads to the following criterion,
( )2
2
8.g
n
i l l l
AT
S u u D−
⎡ ⎤⎢ ⎥≥⎢ ⎥⎣ ⎦
(2.10)
T is the ratio of the turbulent force to the gravity force,
( )( )
12/
,cos
s
l
l g
dP dxT
gρ ρ γ
⎡ ⎤⎢ ⎥=⎢ ⎥−⎢ ⎥⎣ ⎦
(2.11)
13
where the subscript i denotes the liquid film interface and S is the perimeter over which
stresses act.
This map was the first developed that is based on physical principles and allows a
regime map to be constructed that includes the dependence on the pipe diameter, as well
as the pipe orientation and the fluid properties. The drawbacks of this map are the fact
that it does not take into consideration phase change and it has not been calibrated with a
large data set.
ttX Figure 2-3. The Taitel and Dukler flow regime map.
The Steiner Map
The Steiner map [23] is a modified version of the Taitel and Dukler map. The
transition regions have been determined using the same physical principles as those
introduced by Taitel and Dukler [16]. The major improvement of this map over its
counterpart is that the transition curves are adjusted slightly using more advanced
models. A much broader data set was used to calibrate the map. However this map faces
14
a similar drawback to the Taitel and Dukler map in that it does not take into account
phase change.
ttX Figure 2-4. The Steiner flow regime map.
The Wojtan et al. Map
The Wojtan et al. [24] map is the one most recently developed for horizontal flow.
It is a modified form of the map suggested by Kattan et al. [25] that eliminates all
iterative steps. Kattan et al. [25] found that their data for two refrigerants were predicted
more accurately by the Steiner map than any other they used. However the map proved
difficult to use as it involved the evaluation of five different parameters in order to
determine the flow pattern. To alleviate this problem and develop the map into a more
useful design tool, the axes of the Steiner map were converted to mass flux, G, versus
vapor quality, x. In an attempt to improve the accuracy, the transition curves were
15
empirically modified so that the predictions better match the experimental observations.
Kattan et al. [25] were able to transform the map, which was an adiabatic map into a
diabatic one, thus being able to predict partial dryout in annular flow, which was not
possible with earlier maps. Kattan et al. [25] specifically mention that their flow regime
map was developed for vapor qualities higher than 0.15. Wojtan et al. compensated for
this limitation by modifying the transition curves in the low vapor quality (less than
0.327) and low mass flux (less than 200 kg/m2-s) regime based on observations made
with R-22. Details of the map construction are found in the work of Wojtan et al. [24].
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 10
50
100
150
200
250
300
350
400
Annular
Stratified-wavy
Slug
Slug & Stratified-Wavy
Intermittent
Stratified-smooth
x
G (k
g/m
2 s)
Figure 2-5. The Wojtan et al. flow regime map.
Reviews of various flow regime transition maps are given by Frankum et al. [27]
and Spedding and Spence [28]. Frankum et al. [27] suggest that most theoretical maps
perform well over a wide parameter space, while the empirical maps only performed well
for the data set from which it was developed. Spedding and Spence [28] used data
16
collected from co-current water-air horizontal flow experiments through pipes of two
different diameters to show that no one map could satisfactorily predict the flow regime
for the experiments conducted. This underscores the importance of collecting
experimental data on flow regimes that occur during chilldown so that current flow
regime maps can be calibrated or new maps developed.
Forced Convection Boiling Heat Transfer Correlations
It is a widely accepted principle that the heat transfer in flow boiling is a
combination of bulk turbulent convection (macroconvection) and ebullition
(microconvection). This principle was first introduced by Dangler and Addoms [29] in
1956. The influence of these two mechanisms on each other and their effect on the heat
transfer coefficient has been a source of dispute in the past and to date still remains
unresolved.
Dengler and Addoms [29] used a plot of log(h2φ/hl,t) versus log(1/ ttX ) to conclude
that the primary mechanism for heat transfer in flow boiling is the bulk turbulent
transport since the relationship is monotonic as is the case for the two-phase frictional
pressure drop. The two-phase heat transfer coefficient is represented by h2φ, hl,t is the
single-phase heat transfer coefficient based on the liquid fraction flowing, and ttX is the
Martinelli parameter,
0.5 0.10.91 ,v ltt
l v
xXx
ρ µρ µ
⎛ ⎞ ⎛ ⎞−⎛ ⎞= ⎜ ⎟ ⎜ ⎟⎜ ⎟⎝ ⎠ ⎝ ⎠ ⎝ ⎠
(2.12)
in which x is the vapor quality.
17
However, Mesler [30] suggested that Dengler and Addoms misinterpreted their
data. The plot of log(h2φ/hl,t) versus log(1/ ttX ) may be rewritten as log⎥⎥⎦
⎤
⎢⎢⎣
⎡⎟⎟⎠
⎞⎜⎜⎝
⎛∆
⎟⎠⎞
⎜⎝⎛
sat
w
Tq
GAφ2,1
versus log ⎥⎦
⎤⎢⎣
⎡⎟⎠⎞⎜
⎝⎛⎟
⎠⎞
⎜⎝⎛ ∫
z
w dzqGA 0 2,
1φ , where A is the cross sectional area and φ2,wq is
the two-phase wall heat flux. This is essentially a plot of the same quantities against each
other, thus a monotonic relationship is guaranteed regardless of the physical mechanism
involved. By plotting φ2,wq against satT∆ he suggested that the monotonic relationship
was a result of the nucleate boiling phenomenon.
Bergles and Rohsenow [31] incorporated the effects of both the bulk turbulent
convection and nucleate boiling mechanisms by proposing a correlation that predicts the
two-phase wall heat flux by interpolating between the bulk turbulent convection
dominated heat transfer and ebullition dominated heat transfer. The correlation takes the
form,
12 2
, ,,2 ,
, ,
1 1 .w b w ibw w c
w c w b
q qq q
q qφ
⎡ ⎤⎧ ⎫⎛ ⎞⎪ ⎪⎢ ⎥= + −⎜ ⎟⎨ ⎬⎜ ⎟⎢ ⎥⎪ ⎪⎝ ⎠⎩ ⎭⎣ ⎦ (2.13)
Here the subscripts c , b , and ib denote single-phase forced convection, ebullition and
the point of incipient boiling, respectively. This correlation is not utilized often since the
determination of the heat flux due to ebullition is not available without experimentation.
Over the past few decades, numerous correlations have been proposed for
predicting the heat transfer coefficient during forced convection flow boiling. Each
correlation may be classified in one of three categories: superposition, enhancement, or
asymptotic. The most straightforward is the superposition model, which adds the
18
contribution of each mechanism and accounts for the interaction of the mechanisms by
the use of an amplification factor and a suppression factor. The amplification factor is
used to account for the increased turbulent transport in two-phase flow and the
suppression factor is introduced to account for the reduced effective superheat
experienced during ebullition. The second is the enhancement model, which multiplies
the single-phase heat transfer coefficient for the liquid phase along flow in the pipe by the
greater of the contributions between the increased turbulent transport and the ebullition
process. The last model is the asymptotic model. It is termed asymptotic as the value of
the two-phase boiling heat transfer coefficient approaches the larger of the two
components, thus assuring a smooth transition from the convective boiling regime to the
nucleate boiling regime. Many correlations have been developed for horizontal and
vertical flows; however in this study the focus is placed on the horizontal correlations.
The most cited superposition model in the literature is the Chen correlation [32],
originally proposed for vertical flow. In this correlation, the two-phase heat transfer
coefficient is given as,
bl ShEhh +=φ2 , (2.14)
where E is the amplification or enhancement factor and S is the suppression factor. The
single-phase liquid heat transfer coefficient is evaluated using the well-known Dittus-
Boelter equation [33] for turbulent flow,
0.8 0.40.023 Re Pr ,ll l l
khD
⎛ ⎞= ⎜ ⎟⎝ ⎠
(2.15)
where k is the thermal conductivity and the Reynolds number is based on the liquid
fraction flowing,
19
( )l
lDxG
µ−
=1Re . (2.16)
The nucleate boiling heat transfer coefficient is evaluated using the Forster and Zuber
[34] correlation for pool boiling,
( ) ( )0.79 0.45 0.49
0.24 0.75
0.5 0.29 0.24 0.240.00122 ,l pl lb w sat l sat w l
l fg g
k ch T T P P T P
hρ
σ µ ρ⎡ ⎤
= ⎡ − ⎤ ⎡ − ⎤⎢ ⎥ ⎣ ⎦ ⎣ ⎦⎢ ⎥⎣ ⎦
(2.17)
where pc is the specific heat capacity, P is the pressure and the subscript w denotes the
quantity is to be evaluated at the pipe wall. Chen argued that the amplification factor is a
function of the Martinelli parameter and the suppression factor is a function of the two-
phase Reynolds number ( 2Re φ ), and through a regression analysis he determined the
correlation curves for E and S . These correlations were presented graphically and
much later Collier [35] proposed the following curve fits to the graphical correlations for
E and S Eqs. 2.18 – 2.20,
1.01 1 ≤= −ttXforE (2.18a)
1.01213.035.2 1736.0
>⎟⎟⎠
⎞⎜⎜⎝
⎛+= −
tttt
XforX
E (2.18b)
( ) 16 1.1721 2.56 10 ReS φ
−−= + × (2.19)
where the two-phase Reynolds number is determined by,
( )1.252Re Rel Eφ = . (2.20)
A more modern superposition model is the Gungor and Winterton correlation [36].
This correlation has the same form as the Chen [32] correlation, however, a different
model is used for the nucleate boiling heat transfer coefficient and the enhancement
20
factor is taken as a function of both the Martinelli parameter and the Boiling number.
The Boiling number, Bo is defined as,
fg
qBoh G
′′= (2.21)
where q′′ is the heat flux and fgh is the latent heat. The nucleate boiling heat transfer
coefficient, bh , is modeled using the pool boiling correlation of Cooper [37],
( ) 67.05.055.010
12.0 log55 qMPPh rrb−−−= , (2.22)
where M is the molecular weight and rP is the reduced pressure and is equal to the ratio
between the system pressure and the critical pressure. The amplification factor and
suppression factor were determined to be,
86.016.1 137.1240001 ⎟⎟
⎠
⎞⎜⎜⎝
⎛++=
ttXBoE (2.23)
and
17.126 Re1015.111
lExS −+
= . (2.24)
For horizontal flow with Froude number less than 0.05 the amplification factor must be
multiplied by the following factor,
( )lFrlFrE 21.0
1−= (2.25)
and the suppression factor should be multiplied by the following factor,
lFrS =1 (2.26)
where lFr is the Froude number is,
gDGFrl
l 2
2
ρ= . (2.27)
21
By incorporating the heat flux into the enhancement factor it is implied that the nucleate
boiling process further enhances the bulk turbulent convection. This is consistent with
the enhanced frictional pressure drop with increasing heat flux reported by Klausner et al.
[38].
The correlation of Müller-Steinhagen and Jamialahmadi [39] uses a superposition
technique that accounts for the interaction of the convective and nucleate boiling
mechanisms by employing an enhancement factor and a suppression factor. This
formulation absorbs the enhancement factor into the computation of the convective heat
transfer contribution, and the correlation takes the form,
2 .l bh h Shφ = + (2.28)
This correlation employs the correlation of Petukov and Popov [40], for the liquid
phase convective heat transfer coefficient,
( )( )
2
2 3
Re Pr8,
1 12.7 Pr 18
l l
l
l
fkh
fD
φ=
⎛ ⎞+ −⎜ ⎟⎝ ⎠
(2.29)
where the friction factor is given by Filonenko [41],
22(1.82log Re 1.64) .f φ
−= − (2.30)
The two-phase Reynolds number is defined as in Eq. (2.20) and the enhancement factor,
E is given by Eq. (2.18). For flow through annular tubes Eq. (2.29) is multiplied by a
factor
0.16
0.86 .in
out
DD
−⎛ ⎞
Φ = ⎜ ⎟⎝ ⎠
(2.31)
22
The suppression factor is computed by Eq. (2.19). In order to compute the nucleate
boiling contribution to heat transfer, the pool boiling correlation developed by Gorenflo
[42] is used,
0.113
,n
pbp
o o po
Rh qFh q R
⎛ ⎞⎛ ⎞′′= ⎜ ⎟⎜ ⎟ ⎜ ⎟′′⎝ ⎠ ⎝ ⎠
(2.32)
where pR is the surface roughness of the pipe. The pressure function, pF and the
exponent n are calculated using the reduced pressure rP ,
2 22
0.681.73 6.1 .1p r r
r
F P PP
⎛ ⎞= + +⎜ ⎟−⎝ ⎠
(2.33)
Equation (2.33) pertains to water and other low boiling point liquids and is used here; for
the computation of pF for organic liquids reference [39] should be consulted. The
exponent is calculated from
20.9 0.3 ,arn P= − (2.34)
with 0.15a = for water and other low boiling point liquids including nitrogen. The
reference heat transfer coefficient oh , reference heat flux oq′′ , and reference surface
roughness poR for nitrogen are found in [43], and are 210000oWqm
′′ = , 24380oWhm K
= , and
61 10poR m−= × .
One of the most popular enhancement models is the Shah correlation, which was
first developed in graphical form [44] and was later re-established in equation form [45].
Shah proposed that the two-phase heat transfer coefficient might be determined as
follows,
lshh Ψ=φ2 . (2.35)
23
The liquid convective heat transfer coefficient, lh , is evaluated using the Dittus-Boelter
[33] equation, Eq. (2.15), as in the previous models. However, the evaluation of sΨ is
more complicated.
04.0≥= ls FrforCoN (2.36a)
04.038.0 3.0 <= −lls FrforCoFrN (2.36b)
410117.14 −≥= xBoforFs (2.37a)
4101143.15 −<= xBoforFs (2.37b)
where Bo is the boiling number defined previously and Co is the Convection number
given by,
5.08.01⎟⎟⎠
⎞⎜⎜⎝
⎛⎟⎠⎞
⎜⎝⎛ −
=l
g
xxCo
ρρ
. (2.38)
Hence the contribution from the bulk turbulent transport is,
0.8
1.8c
sN−Ψ = (2.39)
and the contribution from the ebullition process is determined as follows,
for 0.1>sN
0.5 5230 3 10b Bo for Bo x −Ψ = > (2.40a)
or
0.5 51 46 3 10b Bo for Bo x −Ψ = + ≤ (2.40b)
for 0.1≤sN
( )0.5 0.1exp 2.74 0.1 1.0b s s sF Bo N for N−Ψ = < ≤ (2.41a)
or
24
( )0.5 0.15exp 2.74 0.1b s s sF Bo N for N−Ψ = ≤ (2.41b)
Thus sΨ is calculated as,
( )max ,s c bΨ = Ψ Ψ . (2.42)
Shah [45] indicates that the equations agree with the graphical representation to within
±6% over most of the chart except in two regions: 1) near 004.0=Co and 41050 −= xBo ,
and 2) for horizontal tubes at 04.0<lFr and 4101 −< xBo . He notes that the equations
overpredict h by approximately 11% in region 1, but should not pose a problem since
these conditions are in the post-dryout region. The inaccuracy in region 2 of
approximately 20% is inconsequential since values below 4101 −< xBo are rarely
encountered in practice. This correlation uses the larger of the two effects in determining
the heat transfer coefficient, thus some of the physics is inevitably lost in the process.
Another enhancement model was developed by Kandlikar [46]. This correlation
expands on the work of Shah [45] with the major advancement being the determination of
a suppression factor and an enhancement factor that depend on not only the boiling
number ( Bo ) but also the convection number (Co ), the Froude number ( lFr ) and a fluid
dependent parameter. The two-phase heat transfer coefficient is predicted as follows,
( )( ) lkCC
lC hFBoCFrCoCh 452
312 25 +=φ . (2.43)
lh is evaluated using the Dittus-Boelter [33] Eq. (2.15). The coefficients 1C through 5C
take different values depending on whether or not the heat transfer is determined to be in
the convective region or the nucleate boiling region, and kF is a parameter that enhances
the nucleate boiling term and represents the fluid-surface combination effect. The values
of these coefficients may be determined from Table 2-1 below.
25
Table 2-1. Empirical constants for the Kandlikar correlation. 65.0<Co (convective region) 65.0≥Co (nucleate boiling region)
1C 1.1360 0.6683
2C -0.9 -0.2
3C 667.2 1058
4C 0.7 0.7
5C 0.3 0.3
kF 0.74 0.74
The Kandlikar correlation has the added advantage of being much simpler to implement
than the Shah [45] correlation.
The asymptotic model was first introduced by Kutateladze [47] in 1961 while he
was describing the influence of forced convection on heat transfer with nucleate boiling
in tubes. He proposed that the heat transfer coefficient is a function of the ratio of the
heat transfer coefficient due to convection and that due to nucleate boiling. This may be
represented as,
⎟⎟⎠
⎞⎜⎜⎝
⎛=
l
b
l hh
fnhh φ2 , (2.44)
where the following conditions hold true,
;0,1,0 === nffnhh
l
b (2.45a)
.1,, →→∞→ nfhh
fnhh
l
b
l
b (2.45b)
The most basic interpolation formula that satisfies these conditions is
n
n
l
b
l hh
hh
⎥⎥⎦
⎤
⎢⎢⎣
⎡⎟⎟⎠
⎞⎜⎜⎝
⎛+= 12φ . (2.46)
26
It was determined from experiments that an acceptable value of n is 2. However, this
correlation does not account for either the enhancement effect or the suppression effect
and thus was modified by a number of investigators to take these effects into account.
A widely cited asymptotic model in the literature is that of Liu and Winterton [48].
This correlation models the two-phase heat transfer coefficient in the following manner,
( ) ( )( )222 bl ShEhh +=φ . (2.47)
They observed that previous correlations, which use the superposition principle,
overpredict the heat transfer coefficient in the high quality region and under predict it in
the low quality region. As a result they selected the asymptotic approach that has the
property of further suppressing nucleate boiling once lEh is appreciably larger than bSh .
As with the previous correlations lh is evaluated using the Dittus-Boelter [33] equation,
Eq. (2.15), however, the Reynolds number in this case is defined as
lfo
GDµ
=Re . (2.48)
The nucleate boiling heat transfer coefficient, bh , is evaluated using the Cooper model
[37] for nucleate pool boiling, Eq. (2.22). The enhancement factor and the suppression
factors are calculated as follows,
35.0
1Pr1⎥⎥⎦
⎤
⎢⎢⎣
⎡⎟⎟⎠
⎞⎜⎜⎝
⎛−+=
g
llxE
ρρ
(2.49)
and
( ) 116.01.0 Re055.01 −+= foES . (2.50)
27
For horizontal flow, the enhancement factor and the suppression factor are modified as
previously mentioned in Gungor and Winterton [36]. Liu and Winterton claimed that this
correlation performs better than those developed previously. However, the improvement
is seen to be marginal.
One correlation developed that cannot be placed explicitly into one of these three
categories is the most recent one developed by Thome [49] and his colleagues. This
correlation is best described as a flow pattern based model, since it is the first to use the
flow structure to determine the portion of the pipe that is in contact with the liquid and
the portion in contact with the vapor and apply a suitable model to the respective region
for horizontal flow. The heat transfer coefficient is thus determined as follows,
( )2
22
dry g dry wetR h R hh
Rφ
θ π θπ
+ −= (2.51)
where R is the internal radius of the pipe, dryθ is the portion of the pipe circumference
that is in contact with the vapor phase and the subscript wet indicates regions in contact
with the liquid. The dry perimeter, dryθ , is determined using a simplified geometric
model for the flow structure. The vapor convective heat transfer coefficient, gh , is
determined using the Dittus-Boelter correlation assuming tubular flow over the dry
perimeter of the pipe,
Dk
h gggg
4.08.0 PrRe023.0= (2.52)
where the Reynolds number with respect to the vapor is
gg
GxDαµ
=Re (2.53)
28
and α is the void fraction. In calculating the void fraction, the Steiner [23] version of the
Rouhani and Axelsson [50] drift flux void fraction model was adopted:
( )( )( ) ( )
10.25
0.5
1.18 111 0.12 1 .l g
g g l l
x gx x xxG
σ ρ ρα
ρ ρ ρ ρ
−⎡ ⎤⎡ ⎤− −⎛ ⎞− ⎣ ⎦⎢ ⎥= + − + +⎜ ⎟⎜ ⎟⎢ ⎥⎝ ⎠⎢ ⎥⎣ ⎦
(2.54)
The heat transfer coefficient, weth , on the wetted perimeter of the pipe is calculated using
an asymptotic equation of the form,
( )1
3 3 3 ,wet b lh h h= + (2.55)
where bh is modeled using the Cooper correlation [37] mentioned previously and lh is
computed using a correlation developed by Kattan et al.[51],
0.69 0.40.0133Re Pr .ll l lkhδ
= (2.56)
Here δ is the simplified film thickness and the Reynolds number is
( ) ll x
xGµ
δ−
−=
1)1(4Re . (2.56)
The simplified film thickness, δ , is determined based on the flow structure shown in
Figs. 2.6 and 2.7.
Figure 2-6. Flow structures used to evaluate stratified flow liquid film thickness and
stratified angle.
29
(a) (b) (c) Figure 2-7. Flow structures used to evaluate (a) annular flow liquid film thickness, (b)
annular flow liquid film thickness and partial-dry out angle, and (c) stratified liquid film with partial dry-out angle.
In order to better model the physical process that occurs in two-phase with heat transfer,
an expression for the onset of nucleate boiling, ONBq was added; the expression gives the
value below which the contribution due to nucleate boiling is not significant. The
criterion employed was developed by Zurcher and coworkers [52],
2 sat lONB
crit g fg
T hqr h
σρ
= (2.57)
in which critr is the critical nucleation radius, and is assigned the value 0.38x10-6 m. This
correlation does not utilize the enhancement factor and the suppression factor as in other
models. Using the asymptotic method for weth weighs the relative importance of the two
effects, however, it is not proven that it correctly accounts for the enhancement and
suppression effects.
The existence of such a large number of predictive models for forced convection
boiling heat transfer highlights the fact that a reliable model that may be applied
universally has not yet been developed. This is clearly illustrated in three recent studies,
each of which identifies a different model as giving the best predictions for the heat
30
transfer coefficient. Greco and Vanoli [53] compared their data for HFC mixtures in
smooth horizontal tubes with a number of correlations including the correlations of Chen
[32], Gungor and Winterton [36], Shah [45], Kandlikar [46], and Thome and coworkers
[49, 51]. They concluded that the best performance was achieved by using the Kandlikar
correlation. Zhang, Hibiki, and Mishima [54] used their data for water, R11, R12 and
R13, and evaluated the correlations of Chen [32], Shah [45], Gungor and Winterton [36],
Kandlikar [46] and Liu and Winterton [48]. The best predictive model for their data
proved to be the Chen correlation. In 2003, Qu and Mudawar [55] carried out
experiments with water in micro-channels and compared the heat transfer data obtained
against the predictive models of Chen [32], Shah [45], Gungor and Winterton [36], Liu
and Winterton [48], and Kandlikar [46]. The correlation of Liu and Winterton out
performed the others.
The predictive models reviewed all agree that the salient factors that influence the
heat transfer in flow boiling is the bulk turbulent convection and ebullition. However, the
manner in which they interact with each other is unclear, hence the existence for such a
large number of correlations. These models have been developed using steady, non-
cryogenic flows, but neither of these conditions applies to the chilldown process. Since
the chilldown process is characterized by rapid transients, pressure fluctuations,
voracious evaporation and large temperature differences, which makes it very difficult to
determine how the two effects responsible for the heat transfer interact.
31
CHAPTER 3 EXPERIMENTAL FACILITY
System Overview
The experimental facility was developed so that the flow structure, the temperature
profile, and the pressure drop may be measured simultaneously. It is illustrated
schematically in Fig. 3-1 below.
Figure 3-1. Schematic of chilldown experimental facility.
Liquid nitrogen was selected as the working fluid for this investigation since it is
chemically inert, colorless, odorless, non-corrosive, nonflammable, relatively
inexpensive, readily available, and poses no significant environmental hazards; the
physical and thermal properties of nitrogen are also well documented. The liquid
T
T T
P dP
dP Vented to environment
Visual Test Section
Nitrogen Supply Tanks
CCD
Collection Tank
Heat Element Ball Valve Temperature Pressure Differential PressureVenturi Heat ExchangerHeat Transfer Section
P dP
T
P
32
nitrogen is stored in high-pressure vacuum jacketed cylinders (at 1587 kPa), the tank
pressure that provides the driving potential for the flow. Once the fluid exits the tank it is
directed through a Joule-Thompson heat exchanger that cools the liquid to ensure that the
nitrogen is in the subcooled state before entering the facility.
Upon entering the facility the flow passes through a 304-stainless steel section (I.D.
12.7 mm, O.D. 15.9 mm, approximate thermal conductivity 16.3 W/m-ºC and specific
heat 0.46 kJ/kg-ºC), which is fitted with a series of external type E (Chromel-Constantan)
thermocouples (3 on the top of the pipe, and 3 at the bottom of the pipe), an internal type
E thermocouple and pressure tap. This allows the inlet flow conditions, and the outer
wall temperature profile to be determined. Following this section, the fluid then enters a
vacuum jacketed visual test section fabricated from pyrex. Here the flow structure is
captured via a CCD (Charge-Coupled Device) camera with appropriate image capturing
software. The nitrogen then passes through another section of piping which contains an
internal thermocouple and a pressure tap, which are used to record the exit conditions at
the exit of the visual test section as well as the pressure drop across it. Once past this
measuring station the fluid enters the heat transfer section of the facility. The section is
38 cm in length between the inlet and outlet; inline thermocouples record the fluid
temperature at these points. A series of thermocouples are placed circumferentially
around the pipe wall and the outer surface for the insulation, which are used to extract the
unsteady heat transfer coefficient information (the details of this procedure is given in a
later section).
A cryogenic ball valve is located after the heat transfer section that allows the flow
to be throttled; thus a wider range of flow rates is attainable. Once through the ball valve,
33
two heaters vaporize any remaining liquid before the flow enters the venturi flow meter.
Then nitrogen is collected in an expansion tank before being vented to the atmosphere via
a ventilation system.
In performing the experiments, the ball valve is set to the desired position, and the
data acquisition system is activated just prior to opening the nitrogen cylinder. All the
measurements, including image capturing, are made electronically and the data are
recorded and displayed in near real time, allowing for immediate experiment feedback,
and determination of the completion of chilldown.
Visual Test Section Design
One of the most vital components of the cryogenic facility is the visual test section.
The visual section consists of a vacuum insulated pyrex tube that is designed to operate
under high pressure (maximum of 1400 kPa) and low temperature conditions (-180 °C)
that exist during chilldown. In order to connect the to the stainless steel tubing pyrex
tube a flange assembly was designed that ensures leak-free operation, see Fig. 3-2.
Figure 3-2. Schematic of the flange assembly.
Goretex Gasket
Teflon O-ring
Test Section
Teflon T
Hex Nut
34
Instrumentation and Calibration
One of the most vital components of the cryogenic facility is the visual test section.
The visual consists of a vacuum insulated pyrex tube that is designed to operate under the
high pressure (maximum of 1400 kPa) and low temperature conditions (-180 °C) that
exist during chilldown. In order to connect the to the stainless steel tubing, a pyrex tube
flange assembly was designed that ensured leak-free operation, see Fig. 3-2.
Static Pressure Transducers
Two Validyne P2-200V pressure transducers are installed in the facility. One is
installed at the inlet to the visual test section so that the inlet pressure ( 1P ) of the fluid
may be determined, while the second on is installed at the inlet to the venturi flow meter
to measure the pressure ( 2P ), which allows for corrections to be made for compressibility
effects. The transducers are rated for 1340 kPa and are independently calibrated using a
mercury manometer. The equation of the calibration curves are given by,
VP ∗+−= 937.274712.271 (3.1)
and
VP ∗+−= 479.276709.302 (3.2)
where 1P and 2P are in kPa and V is the voltage output in volts. The plots of the
calibration curves are given in the work of Velat [56].
Test Section Pressure Drop
The pressure drop ( P∆ ) across the visual test section is recorded using a Validyne
model DP215 variable reluctance differential pressure transducer equipped with a dash-
30 diaphragm (rated for 0.0 to 8.6 kPa). A carrier demodulator device converts the
transducer signal to an analog voltage, and allows the span to be adjusted and signal to be
35
zeroed. The calibration of the transducer was carried out using a manometer with R 827
manometer oil. The equation of the calibration curve is given by,
VP ∗=∆ 2788.1 (3.3)
where P∆ is in kPa and V is in volts; the upper limit on the calibration is 8.2 kPa (the
curve may be seen in the work of Velat [56]). The standard deviation of the calibration is
0.12%, which is within the 0.25% full-scale accuracy listed by the manufacturer.
Flow Meter Calibration
The nitrogen flow rate is measured using a Presco venturi flow meter that has an
inner diameter of 13.9 mm and a throat diameter of 8.73 mm. Proper performance of the
flow meter demands that only nitrogen vapor pass through the instrument; to ensure that
this is the case two 1-kilowatt coil heaters are positioned prior to the flow meter so that
any liquid nitrogen is vaporized before entering the venturi.
A Validyne variable reluctance DP15 differential pressure transducer with a dash-
40 diaphragm (rated for 0.0 to 86.0 kPa) was used to measure the pressure drop across the
venturi; this diaphragm maximizes the sensor output response while providing moderate
overload protection. The differential pressure transducer is coupled to a carrier
demodulator device. The transducer and demodulator device were calibrated using a
mercury monometer, see Velat [56] for calibration curve. The standard deviation of the
differential pressure transducer calibration was 0.17%, which was within the 0.25% full-
scale accuracy claimed by the manufacturer.
Once the transducer was calibrated, the venturi flow meter was calibrated with an
Omega vortex flow meter with compressed air. The actual velocity measured with the
vortex flow meter was plotted against the ideal velocity (see Fig. 3.3) computed with the
36
measured pressure drop and a modified Bernoulli relation [57], which accounted for
compressibility,
⎟⎠⎞
⎜⎝⎛ +
−+++= ...
242
411
21 422
0 MaMauPP γρ , (3.4)
where Ma is the Mach number and γ is the ratio of specific heats.
Ideal Velocity (m/sec)0 50 100 150 200 250 300
Act
ual V
eloc
ity (m
/sec
)
20
40
60
80
100
120
140
160
Compressible Velocity Incompressible Velocity Curve Fit
Figure 3-3. Calibration plot of the actual velocity versus the ideal velocity (Velat [56]).
A polynomial curve, shown in Eq. (3.5), was then fit to the calibration data and used to
correlate the ideal velocity with the actual velocity.
ideal2ideal
3ideal
-5
4-7 u0.5653+u0.0076+u)10(5 -)u10(1 ∗∗∗∗∗= idealactualu (3.5)
Temperature Measurements
Measuring the temperature at various locations in the experimental facility was
vital in understanding and analyzing the chilldown process. The temperature at the inlet
and exit of the visual test section were measured using two 1/16-inch type E (Chromel-
Constantan) thermocouple probes from Omega Engineering. These probes were placed
through precision-drilled holes in line with the fluid and sealed with a combination of
37
brass compression fittings. In order to monitor the chilldown process, a series of 6
(laboratory manufactured) type E (Chromel-Constantan) thermocouples were placed
along the top and bottom of the 304-stainless steel tube prior to the test section, see Fig.
3-4.
Figure 3-4. Thermocouple arrangement on the steel transfer line prior to the visual test
section.
These temperature measurements were used to determine the end of the chilldown
process, which is the point at which the transfer line temperature reaches the saturation
temperature of the liquid nitrogen.
The heat transfer section of the facility is located downstream of the visual test
section and is instrumented with 16 type E (laboratory manufactured) thermocouples.
These were symmetrically positioned around the exterior of the pipe wall and insulation
as shown in Fig. 3-5. The thermocouples were placed in such a manner that the exterior
thermocouples that were secured to the insulation were exactly at the same angular
positions as the interior thermocouples that were secured to the pipe wall. Each group of
thermocouples is separated by an axial distance of 9.0 cm and is secured to the insulation
38
and the pipe wall with 0.25-inch Teflon tape, to ensure proper thermal contact. At the
inlet and exit of the heat transfer section, thermocouple probes, separated by an axial
distance of 35.5 cm, were used to evaluate the change in fluid temperature as it passed
through the section. The temperature data obtained were used to calculate the unsteady
heat transfer coefficient.
Figure 3-5. Thermocouple placement for heat transfer test section.
Once through the heat transfer test section the flow passes through the venturi flow
meter, which is instrumented with an inline type E thermocouple. The temperature and
pressure information at this location are used to correct for any compressibility effects.
The temperature readings were accurate to ±1.7°C over the large temperature range
experienced in these experiments.
Data Acquisition System
A digital data acquisition system was assembled to record and process the analogue
output of the instrumentation. The system consists of a personal computer outfitted with
an analog to digital data acquisition board and accompanying data acquisition software.
The computer is equipped with an AMD Athlon XP 2200 MHz processor board in
combination with 15 Gigabits of random access memory. The analog-to-digital board
39
was a Measurement Computing PCIM-DAS1602/16 with 8 channels and 16 bit
resolution and was connected to two Measurement Computing CIO-EXP32 multiplexer
boards. These two multiplexer boards allow for 64 analog inputs/channels. Each board
is divided into two banks of 16 channels each. The gain for each bank of 16 may be set
independently, and as such the gain for the thermocouple signals was set to 100 while the
gain for the pressure transducers was set to 1. The reference temperature for
thermocouple readings was obtained from an on board junction temperature that was
input to the analog-to-digital board through a selected channel. All channels through
which thermocouple measurements are taken are provided with a 1µF capacitor across
the high and low inputs forming a low-pass filter having a 7 Hz filtered cutoff. Open
thermocouple detect, and a reference to ground through a 100 k-ohm resistor are also
provided. The analog-to-digital board and each multiplexer board were calibrated to the
manufacture’s specifications using the supplied software, InstaCal.
A computer program was developed, using Softwire, to measure and record the
experimental data. The program sampled each channel at a frequency of 50 Hz, and
compiled these readings in a series of distinct arrays. At the completion of the 50th
recording, the arrays were time averaged, and transferred to an Excel spreadsheet where
further data processing was carried out. In the Excel spreadsheet, the temperature and
pressure data were processed to obtain the mass flux, Mach number, vapor and liquid
velocities, vapor and liquid densities, and vapor and liquid Reynolds numbers.
Digital Imaging System
A digital imaging facility was constructed to capture the flow structure as it passed
through the visual test section. The imaging system was comprised of a Pulnix TM-
40
1400CL progressive scan CCD (capable of capturing images with 1392 x 1040 pixel
resolution), with a 50 mm Canon magnification lens, connected to a Data Translation
DT-3145 framegrabber board via a Camera Link cable. Images were captured using the
Global Imaging Lab software provided by Data Translation, which not only records the
images but also allows for the image to be calibrated so that accurate length
measurements may be made. The visual data allowed for the flow regime and vapor
volume fraction to be determined.
Experimental Protocol
Once the experimental facility was constructed it was used to investigate the
cryogenic chilldown process. Experiments are carried out in the following manner:
• The data acquisition program is activated so that it may commence recording at the push of a button.
• The imaging program is activated so that it may begin capturing the flow structure at the push of a button.
• The nitrogen tank connected to the heat exchanger shell-side is opened.
• The nitrogen tank connected to the facility is opened to a predetermined position and the data acquisition program and imaging program are started.
• Liquid nitrogen is allowed to flow through the facility until all thermocouples that are in contact with the pipe wall read the saturation temperature of the liquid nitrogen; at that point it is concluded that the chilldown process is complete.
• The temperature, pressure and mass flow rate are recorded as described prior.
• The flow structure images are recorded as described prior. The liquid film thickness is measured from the flow structure images using the Global Imaging Lab software from the information recorded.
• The above steps are repeated with the throttling valve in different positions so that a wide parameter range may be investigated.
In the following chapter the data reduction method will be presented.
41
CHAPTER 4 DATA PROCESSING
Vapor Quality Estimation
The direct computation of the vapor quality using an energy conservation approach
was not employed because there is a substantial amount of energy transfer into the
nitrogen that is not easily quantified. In order to obtain an approximation for the vapor
quality, a correlation between the vapor volume fraction and the vapor quality is utilized.
One of the simplest models that correlates vapor quality and vapor volume fraction is the
slip velocity model. The slip velocity, S , is the ratio of the mean vapor velocity to the
mean liquid velocity and can be expressed as,
11
l
g
xSx
ραα ρ
⎛ ⎞−⎛ ⎞⎛ ⎞= ⎜ ⎟⎜ ⎟⎜ ⎟⎜ ⎟−⎝ ⎠⎝ ⎠⎝ ⎠. (4.1)
The above expression may be rearranged to express vapor volume fraction as a function
of quality and slip velocity, as in Eq. (4.2), or it may be rearranged to express the quality
as a function of the vapor volume fraction and the slip velocity, as in Eq. (4.3).
( ),
1 g
l
x
x S xα
ρρ
=⎛ ⎞
+ − ⎜ ⎟⎝ ⎠
(4.2)
( ).
1 g
l
SxS
αρ
α αρ
=⎛ ⎞
+ − ⎜ ⎟⎝ ⎠
(4.3)
42
The slip velocity model is limited to situations in which the slip velocity remains
relatively constant, and this is not the case for the chilldown process. Instead a different
correlation for relating the vapor volume fraction to the vapor quality is employed.
In 1965, Zuber and Findlay [59] developed a more practical model to correlate the
vapor quality and the vapor volume fraction. The model was derived by considering the
local volumetric fluxes of the liquid and vapor phases together with the mass continuity
equations of the two phases. It was determined that the vapor volume fraction and the
vapor quality are related by,
01 11 g g
vjl
xC Ux Gx
ρ ρα ρ
⎡ ⎤−= + +⎢ ⎥
⎣ ⎦, (4.4)
where 0C and vjU are empirical constants. The distribution parameter, 0C , which
accounts for non-uniform flow and concentration profiles, and vjU accounts for the effect
of the local relative velocity. Eq. (4.4) may be rearranged to give,
( )0
0 01
g vj
g
l
U C GxG C C
α ρρ
α αρ
+=
⎛ ⎞− +⎜ ⎟
⎝ ⎠
(4.5)
It was demonstrated by Klausner [60] that assigning values of 0.10 =C and 0.6vjU = for
horizontal flow, give excellent agreement: within ± 5% for over 90% of the horizontal
two-phase flow data with R113 as the working fluid. Due to the excellent agreement
with the horizontal flow experiments of Klausner [60] using R113, Eq. (4.5) was used to
estimate the vapor quality from the measured vapor volume fraction.
43
Vapor Volume Fraction
The vapor volume fraction α is an important parameter that must be determined
when analyzing two-phase flows. This is underscored by the fact that many different
experimental methods have been developed to compute this quantity. Methods vary from
using gamma radiation absorption and laser dispersion techniques to visual techniques.
For this study, digital images of the flow structure were recorded; thus a visual technique
is adopted.
In order to compute the vapor volume fraction, the flow regime must first be
identified. Researchers have used a number of different conventions to describe the
various flow structures observed in horizontal two-phase flows; the convention used here
is the one described by Carey [58] and is illustrated in Fig. 2.1. Once the regime is
determined one of the following approaches is used to compute the vapor volume
fraction.
If the flow regime is classified as stratified, wavy or intermittent the liquid height is
measured using the Global Imaging Lab software from the images as shown in Fig. 4.1.
The vapor volume fraction is calculated,
( )2 2
2
cos 21
rr A r h rr
r
δ δ δα
π
⎛ − ⎞⎛ ⎞ − − −⎜ ⎟⎜ ⎟⎝ ⎠⎜ ⎟= −⎜ ⎟⎜ ⎟⎝ ⎠
. (4.6)
For the case of annular, and plug flow, the flow structure is modeled as shown in
Fig. 4-2. The liquid film thickness at the top, topδ , and bottom, bottomδ , of the tube are
measured and the vapor volume fraction is calculated as
44
2
221 ⎟⎟
⎠
⎞⎜⎜⎝
⎛−−=
rrtopbottom δδ
α . (4.7)
δ
Figure 4-1. Model used for the stratified, wavy and intermittent flow volume fraction
computation.
Figure 4-2. Diagram of the model used for the annular flow volume fraction computation.
Extracting the Heat Transfer Coefficient
In order to extract the heat transfer coefficient from the temporal profile of wall
temperature; an inverse procedure is employed which varies from that of traditional
inverse heat conduction methods. It does not require a system of least-square equations
to be solved. Some of these traditional methods are reviewed by Ozisik [61].
45
The process used here for extracting the transient heat transfer coefficient on the
inside of the pipe involves a number of iterative procedures, which are reported here as
three major steps. These steps are illustrated in Fig. 4-3 and are carried out for each
instance of time. These steps include (1) guess the heat transfer coefficient on the inside
of the pipe, (2) knowing the heat transfer coefficient on the outside of the pipe via
calibration, the temperature field is calculated, and (3) the temperatures calculated at the
outer wall are then compared with those measured. If the temperatures match, the
guessed heat transfer coefficient is taken as the actual heat transfer coefficient, otherwise
a new guess is made and the process is repeated until the computed and measured
temperatures match.
Guess the heat transfer coefficient inside the pipe
Solve the heat conduction equation in the pipe wall
Check if computed temperatures and measured temperatures at
the outer surface match
Do temperatures match?
Record the heat transfer coefficient
yes
no
Figure 4-3. Flow chart for transient heat transfer coefficient extraction.
46
Computing the Temperature Field in the Pipe Wall
The unsteady 3-D form of the heat conduction equation in cylindrical coordinates,
see Fig. 4-4, is written as follows:
1 1p
T T T k Tc ρ k rkt z z r r r r rφ φ
⎛ ⎞∂ ∂ ∂ ∂ ∂ ∂ ∂⎛ ⎞ ⎛ ⎞= + + ⎜ ⎟⎜ ⎟ ⎜ ⎟∂ ∂ ∂ ∂ ∂ ∂ ∂⎝ ⎠ ⎝ ⎠ ⎝ ⎠, (4.8)
where ρ is the density of the material, pc is the specific heat capacity, t is the time
variable, T is the temperature, r is the radial coordinate, z is the axial coordinate and φ
is the azimuthal coordinate. This equation is non-dimensionalized using the following
parameters:
sat
w sat
T TT T
ϕ−
=−
; zzd
= ; rrd
= ; 0
pp
p
cc
c= ;
0
kkk
= ; 0
,ρρρ
= (4.9)
where satT is the saturation temperature of the fluid within the pipe, wT is the temperature
on the outer wall of the pipe, d is the pipe wall thickness, and the subscript 0 denotes the
property is to be evaluated at the initial temperature, 0T . Thus the original equation is
transformed to
20 0
0
1 1 .c d kc k rkk t z z r r r r r
ρ ϕ ϕ ϕ ϕρφ φ
⎛ ⎞∂ ∂ ∂ ∂ ∂ ∂ ∂⎛ ⎞ ⎛ ⎞= + + ⎜ ⎟⎜ ⎟ ⎜ ⎟∂ ∂ ∂ ∂ ∂ ∂ ∂⎝ ⎠ ⎝ ⎠ ⎝ ⎠ (4.10)
The temperature variations experienced by the pipe during the chilldown process
are significant, and thus the thermal properties ( k and c ) of the pipe material vary
significantly. These variations are taken into account by assigning the thermal properties
as a function of the temperature at any given point.
A finite volume formulation is used to disceritize Eq. (4.10); a backward Euler
scheme is employed for the temporal term and a central difference scheme is used for the
47
spatial terms. The system of equations that result are solved using the Alternating
Direction Implicit (ADI) method described in [62].
In order to solve the system of equations, the energy entering the system from the
ambient must be known; hence the heat transfer coefficient for the outside surface of the
ϕ
z
r
dodiDin Dout
Figure 4-4. Coordinate system for heat conduction through the pipe wall.
pipe insulation must be determined. This is accomplished through a steady-state
calibration process in which cool nitrogen vapor is passed through the heat transfer
section at various mass flow rates. A relationship between heat flux through the pipe
insulation versus temperature difference (ambient temperature less the insulation surface
temperature) is determined. A constant heat transfer coefficient is approximated as
shown in Fig. 4-5. The slope of the line is the heat transfer coefficient for the outer pipe
surface. The measurement of the heat flux into the pipe, wq″ , is quite difficult to measure
due to the small temperature rise in the cryogenic vapor; thus there is some scatter in Fig.
4-5. However, the measured heat transfer coefficient, 4.38 W/m2-K, is quite small,
48
compared with convective heat transfer on the inner pipe wall. The errors in the
calibration have a negligible impact on the computed thermal field in the pipe wall.
The boundary condition for the outer pipe surface is written,
( ) ,out outTk h T Tr ∞
∂− = −
∂ (4.11)
∆T (K)
q w”(
W/m
2 )
Figure 4-5. Calibration for determining the outer pipe surface heat transfer coefficient.
which is non-dimensionalized to give,
0 0
.out out sat out
w sat
h d h T h Tdkr k k T Tϕ ϕ ∞⎛ ⎞−∂
− = + ⎜ ⎟′∂ −⎝ ⎠ (4.12)
Here subscripts out and ∞ denote the outer surface of the pipe, and the outer insulation
surface, respectively. The inner pipe boundary condition is written as,
( ) ,in in flTk h T Tr
∂− = −
∂ (4.13)
which is then non-dimensionalized to give,
0 0
in sat in flin
w sat
h T h Th d dkr k k T Tϕ ϕ
−⎛ ⎞∂− = + ⎜ ⎟∂ −⎝ ⎠
(4.14)
49
Here the subscripts i and fl denote the inner surface of the pipe and the fluid flowing
through the pipe, respectively. The fluid temperature is determined using an internal
thermocouple that measures the temperature at the inlet of the heat transfer section.
The heat transfer coefficient on the inside of the pipe, inh , is the quantity that is
guessed during the calculation. The two-phase flow structure present for much of the
experiment is stratified, and there is a significant difference between the temperature at
the top of the pipe and the temperature at the bottom the pipe. This must be due to
circumferential variations in the heat transfer coefficient. This problem is dealt with
adequately by dividing the interior surface of the pipe into three distinct sections within
which the heat transfer coefficient is assumed constant. Region 1 is such that 10 α α≤ < ,
and in toph h= , region 2 is such that 1 2α α α≤ < , and in sideh h= , and region 3 is such that
2 3α α α≤ ≤ , and i bottomh h= (see Fig. 4-6). In the film boiling regime it is adequate to
allow all three regions to be equal in size, hence, 1 2 1 2α α α π α= − = − . However in the
nucleate boiling regime, where the temperature at the bottom changes suddenly by a
significant amount very high heat transfer coefficients are present. Hence it is important
not to overestimate the size of the region in which nucleate boiling occurs. If the region
is overestimated then the amount of energy removed from the pipe would be too large in
the adjacent region (in this case region 2) making it impossible to match the outer wall
temperature. This is handled adequately by reducing the size of region 3 by increasing
the value of 2α . When necessary, it is sufficient to reduce the size of region 3 by a factor
of 2. For modeling purposes, a more systematic approach to describing different regions
during nucleate boiling is desirable. However, the present approach is sufficient to match
the measured and computed wall temperature variations.
50
Iteration Process for Guessing the Inner Heat Transfer Coefficient
Any number of methods may be used to obtain a new guess for the inner heat transfer
coefficient; a systematic method for iterating is recommended. In this work after the
initial guess is made subsequent guesses are determined using linear interpolation or
1α
2α
π
Region 1hin=htop
Region 2hin=hside
Region 3 hin=hbottom
α
Figure 4-6. Assumed variation of heat transfer coefficient on the inside surface of the
pipe.
linear extrapolation. Hence the new guess for inner heat transfer coefficient is given by,
( ) ,pres prevnew known prev prev
pres prev
h hh T T h
T Tε
⎛ ⎞−= − +⎜ ⎟⎜ ⎟−⎝ ⎠
(4.15)
where ε is a scaling factor that reduces oscillations and takes the value 0.3 in this work.
The subscripts pres , prev , new , and known denote the present, previous, new, and
known quantities respectively.
Test for Convergence
The final step in the process is checking the computed temperature against the
measured temperature. This is done using the temperatures at the top, side and bottom of
the pipe. Once the computed temperature is within ±1x10-8 K, the temperatures are
51
considered a match. Care must be taken when determining the limit within which to
consider the temperatures to be matched; if the value selected is too small the
computation time increases significantly and the marginal improvement in accuracy does
not justify the increased computational cost.
Computational Code: Testing and Verification
Stability of Computational Code
For simplicity the stability criterion is developed using the Von Neumann analysis
of the 1D heat conduction equation,
2
2
xu
tu
∂∂
=∂∂ α (4.15)
where u is the dependent variable, t is the time, x is the spatial parameter and alpha is the
thermal diffusion. Eq. (4.15 ) is discretized using a backward in time and central in space
scheme.gives
( )( )
11 1 11 12 2
n nj j n n n
j j j
u uu u u
t xα+
+ + ++ −
−= − +
∆ ∆ (4.16)
where n is the index representing time, and j is the index representing space. The
stability analysis of this scheme may be found in any classical numerical methods text,
and proves that the scheme is unconditionally stable. This is also true for the 2D and 3D
schemes.
Grid Resolution
The grid resolution is as an important factor when considering the accuracy of the
solution obtained from numerical computations. Thus, the influence of grid resolution on
the computed heat transfer coefficient is assessed by examining the average percentage
error obtained when various size grids are utilized. A single-phase flow simulation with
52
a constant heat transfer coefficient is used to compute the outer wall surface temperature
for a series of 50 time steps. The physical parameters are as follows: 1) pipe density =
8000 kg/m3, 2) pipe specific heat capacity = 500 J/kgK, 3) pipe thermal conductivity =
16.2 W/mK, 4) inner diameter of pipe = 12.5mm, 5) thickness of pipe = 1.65 mm, and 6)
time step size = 0.1 sec. The inverse procedure is then applied to this series of
temperature values to extract the heat transfer coefficient. This is done using various size
grids. The average percentage error is computed as,
( )1
1 100,N
actual extracted
i actual
abs h hAverage percentage error
N h=
−= ×∑ (4.17)
where N is the number of time steps. The results are given in Table 4-1.
Table 4-1. Influence of grid resolution on the computed heat transfer coefficient. Nx Ny Average percentage error (%) 120 64 0.000729
60 32 0.003904
30 16 0.01681
From Table 4-1 we see that the refinement of 60x32 or better gives an error of less
than 4 x 10-3%. Hence no significant error is introduced once the grid resolution is better
than 60x32. For this study we have chosen to use a refinement of 60x32 as it is gives
good results with little additional computational cost. From Fig. 4-7 we observe that the
approach s second order accurate, which is consistent with the numerical scheme
employed.
Testing the Inverse Procedure
In order to assess the performance and validity of this inverse method, it is first
used to calculate the heat transfer coefficients for a single-phase flow simulation in which
the heat transfer coefficient is known and varies in time. Second it is used to calculate the
actual heat transfer coefficient for single-phase nitrogen gas flowing through the
53
y = -2.2636x + 3.6496
-7.5
-7
-6.5
-6
-5.5
-5
-4.5
-4
-3.5
-33 3.2 3.4 3.6 3.8 4 4.2 4.4 4.6 4.8 5
LN(Grid Size)
LN(A
vera
ge E
rror
)
Figure 4-7. Ln(Error) vs ln(grid size) for the inverse technique.
experimental facility, with the results being compared with the predictions of the Dittus-
Boelter correlation for cooling. Finally, it is used to calculate the heat transfer coefficient
for a single phase flow simulation undergoing a step change in heat transfer coefficient.
In the first test case, the heat transfer coefficient follows a parabolic path with time. A
comparison of the specified heat transfer coefficient with that extracted using the inverse
method is shown in Fig. 4-8 (the time step size used in this test is 0.1 sec; all other
parameters are as specified previously). In Fig. 4-8 it is seen that a parabolic varying heat
transfer coefficient is captured quite reliably with the inverse approach. The difference
between the exact and the extracted heat transfer coefficients for this case are shown in
Fig. 4-9. It is seen that error is not significant and it is of interest to note that the error is
largest in regions where the rate of change of temperature with time are largest. A
comparison of the extracted single-phase heat transfer coefficient with the Dittus-
Beoelter correlation for flowing nitrogen gas is shown in Fig. 4-10 (the time step size
used in this test is 1 sec since that is the smallest time interval for which reliable data
54
could be obtained; all other parameters are as specified previously). The comparison is
quite good. The heat transfer coefficient is not constant with time since the mass flux
fluctuates around a mean of 196 kg/m2-s.
Figure 4-11 illustrates the performance of the inverse procedure in a case where
there is a step change in the heat transfer coefficient (the time step size used in this test is
0.1 sec; all other parameters are as specified previously). It is observed that the inverse
procedure is capable of handling a step change in heat transfer coefficient satisfactorily.
In order to assess the sensitivity of the procedure to errors in the experimental
measurements of pipe wall temperature, ±0.2oC errors were artificially added to the
measured data, and the heat transfer coefficient extraction procedure is applied. The
value ±0.2oC is the repeatability of the thermocouple measurements, and since the
extracted heat transfer coefficients depend on the temperature difference between
successive time instances, the error associated the temperature difference is also expected
to be of this order. It was found that the perturbation of ±0.2oC resulted in a maximum
deviation of ±6% in the value of the heat transfer coefficient extracted. Hence the
inherent variations in thermocouple measurements do not significantly affect the
extracted heat transfer coefficients.
The inverse technique is next applied to the experimental data for the chilldown
process in the nucleate boiling regime. The unsteady heat transfer coefficients on the
inner surface of the pipe are extracted over regions 1, 2, and 3.
55
0
50
100
150
200
250
300
350
0 2 4 6 8 10 12 14 16 18 20
Time (sec.)
Hea
t Tra
nsfe
r Coe
ffici
ent (
W/m
2 K)
Actual heat transfer coefficientExtracted heat transfer coefficient
Figure 4-8. Computation of a parabolic varying heat transfer coefficient using the inverse
method.
-0.004
-0.003
-0.002
-0.001
0
0.001
0.002
0.003
0.004
0 2 4 6 8 10 12 14 16 18 20
Time (sec.)
Diff
eren
ce B
etw
een
Act
ual a
nd E
xtra
cted
Hea
t Tra
nsfe
r C
oeffi
cien
t (W
/m2 K
)
Figure 4-9. Difference between the exact heat transfer coefficient and the heat transfer
coefficient extracted using the inverse technique for the parabolic varying heat transfer coefficient simulation given in Fig 4-8.
56
Dittus-Boelter correlationInverse model
Tbulk = 174 oK
G = 196 kg/m2-sG
Figure 4-10. Comparison of heat transfer coefficient computed using the inverse
procedure and the Dittus-Boelter correlation for single-phase nitrogen gas flow.
0
500
1000
1500
2000
2500
0 0.5 1 1.5 2 2.5 3 3.5 4Time (sec.)
Hea
t Tra
nsfe
r Coe
ffici
ent (
W/m
2 K)
Actual Heat Transfer CoefficientExtracted Heat Transfer Coefficient
Figure 4-11. Computation of a step change in heat transfer coefficient using the inverse
method.
57
CHAPTER 5 CHILLDOWN FLOW TRANSITION AND HEAT TRANSFER
Upon introducing the liquid nitrogen into the facility, heat stored in the pipe walls
vaporizes the in-coming fluid. As more liquid enters the facility a liquid film is observed
to travel through the pipe supported on top of a vapor layer. This is the film boiling
regime. As the pipe wall cools it eventually reaches the Leidenfrost temperature at which
point nucleate boiling ensues resulting in a much higher heat transfer rate. This transition
between the film boiling regime and the nucleate boiling regime is marked by the
quenching front which is shown in Fig. 5.1.
Figure 5-1. Quenching front that marks transition for film boiling to nucleate boiling
The data from two experiments are shown in Figs. 5.2 and 5.3, for various
circumferential positions on the outer wall of the pipe (the top, the bottom, and the left
and right sides). These measurements are recorded on the outer wall of the pipe in the
58
first station of the heat transfer section, which is located approximately one meter down
stream of the visual test section. Fig. 5-2 gives the temperature profile for a low mass
flux experiment, 75 kg/m2s (the actual mass flux data is shown in Fig. 5-4); while Fig. 5-
3 gives the temperature profile for a moderate mass flux experiment, 210 kg/m2s (the
actual mass flux data is shown in Fig. 5-5). By examining Figs. 5-2 and 5-3 it is seen that
the heat transfer process passes through two distinct regimes, which are the film boiling
regime and the nucleate boiling regime. The film boiling regime is seen to have a lower
heat transfer rate than for the nucleate boiling regime, which is illustrated by different
temperature gradients in the two regions. It is also observed that at higher mass flow rates
the chilldown time is shorter, which is expected since there is a higher rate of thermal
transport.
-200.00
-150.00
-100.00
-50.00
0.00
50.00
0 20 40 60 80 100 120 140 160 180Time (sec)
Tem
pera
ture
(C)
Temp 1 (Top)Temp 2 (Left)Temp 3 (Bottom)Temp 4 (Right)
Stratified / Wavy
Figure 5-2. Temperature profile during chilldown for low mass flux experiment.
59
-200.00
-150.00
-100.00
-50.00
0.00
50.00
0 20 40 60 80 100 120Time (sec)
Tem
pera
ture
(C)
Temp 1 (Top)Temp 2 (Left)Temp 3 (Bottom)Temp 4 (Right)
Stratified / Wavy
Slug Plug
Figure 5-3. Temperature profile during chilldown for moderate mass flux experiment.
0.00
20.00
40.00
60.00
80.00
100.00
120.00
0 20 40 60 80 100 120 140 160 180Time (sec)
Mas
s Fl
ux (k
g*m
^2/s
ec)
Stratified / Wavy
Figure 5-4. Transient mass flux for low mass flux experiment.
60
0.00
50.00
100.00
150.00
200.00
250.00
300.00
0 20 40 60 80 100 120Time (sec)
Mas
s Fl
ux (k
g*m
^2/s
ec)
Stratified / Wavy Slug Plug
Figure 5-5. Transient mass flux for moderate mass flux experiment.
0.0
0.2
0.4
0.6
0.8
1.0
1.2
0 20 40 60 80 100 120 140 160 180
Time (sec)
Vapo
r Vol
ume
Frac
tion
Stratified/Wavy
Figure 5-6. Transient vapor volume for low mass flux experiment.
61
0.0
0.2
0.4
0.6
0.8
1.0
1.2
0 20 40 60 80 100 120Time (sec)
Vapo
r Vol
ume
Frac
tion
Stratified/Wavy Slug Plug
Figure 5-7. Transient vapor volume fraction for moderate mass flux experiment.
0.0
0.2
0.4
0.6
0.8
1.0
1.2
0 20 40 60 80 100 120 140 160 180
Time (sec)
Qua
ltiy
Stratified/Wavy
Figure 5-8. Transient vapor quality for low mass flux experiment.
62
0.0
0.2
0.4
0.6
0.8
1.0
1.2
0 20 40 60 80 100 120Time (sec)
Qua
ltiy
Stratified/Wavy Slug Plug
Figure 5-9. Transient vapor quality for moderate mass flux experiment.
It must be noted that the mass flux data collected at the start of the experiment may
not be reliable. In the instances when the storage tank pressure is high a shock is
generated when the valve is initially opened. This causes large pressure oscillations
which leads to erroneous mass flux readings from the venture flow meter, which uses
pressure to determine the mass flux. This is evident in Fig. 5-10, which displays the inlet
pressure profile for the low mass flux experiment. The moderate mass flux experiment
also exhibits this behavior, however it is more mild than the low mass flux case, which is
evident from Fig. 5-11.
Flow Regimes
The detailed momentum and heat transfer processes that evolve during transient
chilldown are not well understood, which limits the development of advanced
hydrodynamic and thermal models. Knowledge of the flow structure is essential to
63
predicting the non-uniform temperature fields encountered during the film and nucleate
boiling heat transfer regimes. A satisfactory flow regime transition map has yet to be
0
200
400
600
800
1000
1200
1400
0 20 40 60 80 100 120 140 160 180
Time (sec)
Pres
sure
(kPa
)
Figure 5-10. Transient inlet pressure profile for low mass flux experiment.
0
100
200
300
400
500
600
700
800
900
1000
0 20 40 60 80 100 120
Time (sec)
Pres
sure
(kPa
)
Figure 5-11. Transient inlet pressure profile for moderate mass flux experiment.
64
developed that address the cryogenic chilldown process. The experiments carried out
allow the flow regime transitions encountered during transient cryogenic chilldown in a
horizontal pipeline to be observed and recorded. The observations are compared with
well known flow regime maps described in chapter 2.
Experimental Observations
The flow pattern names and corresponding flow structures observed during this
investigation are shown in Fig. 2-1. Experiments are carried out for mass fluxes that
range from 66 to 625 kg/m2-s; and vapor qualities vary from 0.004 to 1. The entire
database consists of 2625 data points and is available in Excel format from the author.
When the liquid nitrogen first enters the flow facility a film boiling front is positioned at
the entrance to the facility. This film boiling front produces voracious evaporation
accompanied by a high velocity vapor front traversing down the test section. The vapor
flow is typically entrained with a very fine mist of liquid to produce a mist flow. The
mass flux through the system rises very rapidly, but is constrained by the fact that the
flow becomes choked due to the high velocity vapor flow. Typical profiles of the mass
flux are shown in Figs. 5-4 and 5-5. At low to moderate mass fluxes (usually below 350
kg/m2-s), a stratified-wavy flow structure with a thin liquid film is seen to flow through
the pipe once the film boiling front has passed through the test section. At this point the
flow is in the film boiling regime, and a thin layer of vapor exists between the liquid film
and the pipe wall; hence the heat transfer is mainly the result of thermal conduction
through the vapor layer. As the pipe chills, the liquid film thickness grows. The flow
transitions from film boiling to nucleate flow boiling when the pipe wall temperature falls
below the Leindenfrost temperature. This transition is characterized by the sudden and
steep increase in the slope of the wall temperature history profile shown in Figs. 5-2 and
65
5-3. This transition to nucleate flow boiling is observed visually as a quenching front that
propagates through the pipeline. As the pipe cools further, the flow structure transitions
from the stratified-wavy regime to the intermittent regime. Once the pipe wall
temperature reaches the saturation temperature of the nitrogen, the flow transitions to
single-phase liquid flow. At higher mass fluxes (usually above 350 kg/m2-s), the initial
mist flow structure transitions into annular flow following the passage of the film boiling
front. The later flow transitions include intermittent and single-phase liquid flow.
The mass flux, shown in Figs. 5-4 and 5-5, and vapor volume fraction profiles,
shown in Figs. 5-6 and 5-7, highlight the inherent unsteady nature of the chilldown
process. The vapor volume fraction was computed from the digital images of the flow
structure and smoothed by finding the best smooth curve fit to the measurements, as
outlined in Chapter 4. The computed vapor quality profile is illustrated in Figs. 5-8 and
5-9.
Performance of Current Flow Regime Maps
Modern phenomenological two-phase flow models rely on knowledge of the flow
structure for a prescribed operating condition. Three different well known flow pattern
maps are tested against the experimentally observed flow regimes for horizontal
cryogenic flow chilldown. These include flow regime maps proposed by Baker [19],
Taitel and Dukler [16], and Wojtan et al. [24]. All of these flow regime maps were
developed for quasi-steady two-phase flow. They do not attempt to account for the
transients encountered during chilldown.
Van Dresar and Siegwarth [63] reported flow patterns for low mass flux (97-346
kg/m2s) steady two-phase flow of nitrogen through a horizontal pipeline. The data of
Van Dresar and Siegwarth [63] are compared against the flow regime predictions from
66
the three maps discussed. Only turbulent flow data are considered. Comparisons with
the Baker map, shown in Fig. 5-12, are rather fortuitous, as it is observed that the flow
patterns are correctly predicted with the exception of 2 points, which lie close to the
correct flow pattern regime. It is observed in Fig. 5-13 that the Taitel and Dukler map
performs reasonably well, as all the data points lay within or close to the predicted flow
pattern. The Wojtan et al. map is able to predict slug flow which is considered to be
intermittent flow; however it is unable to predict the annular data, as shown in Fig. 5-14.
The flow regime transition maps are now applied to the data obtained for the
chilldown process, which at times may have significantly larger mass fluxes than the
experiments reported by Van Dresar and Siegwarth [63]. The entire database consists of
2625 data points. Table 5-1 provides a sample of 40 data points from the assembled
database, which covers the entire range of parameters. For the purpose of clarity, the
flow regime maps are compared against a representative set of data consisting of 400 data
points. These 400 data points cover the entire range of flow parameters and flow
structures. They are chosen to avoid excessive clustering of points in the flow regime
maps that occur when the entire database is used.
A comparison of the data with the Baker map is shown in Fig. 5-15. It is observed
that the intermittent data are predicted reasonably well, but neither the annular nor the
stratified-wavy predictions give satisfactory agreement with the data. Fig. 5-16 shows a
comparison of the experimentally observed flow regimes with those predicted using the
Taitel and Dukler map. Although, many observed flow regimes differ from those
predicted, the agreement could be greatly improved with calibration. A comparison of
the data with Wojtan et al. map is shown in Fig. 5-17. While the stratified-wavy and the
67
Wavy Annular
Dispersed
BubblySlug
Plug= intermittent= annular= stratified-wavy
Figure 5-12. Comparison of Van Dresar and Siegwarth data with the Baker map.
10-2 10-1 100 101 10210-3
10-2
10-1
100
101
Stratified-wavy
Stratified-smooth
Intermittent
BubblyAnnular
= intermittent= annular= stratified-wavy
Xtt
TF
K x 10-3
Figure 5-13. Comparison of Van Dresar and Siegwarth data with the Taitel and Dukler
map.
68
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 10
50
100
150
200
250
300
350
400
Annular
Stratified-wavy
Slug
Slug & Stratified-Wavy
Intermittent
Stratified-smooth
x
G (k
g/m
2 s)
= intermittent= annular= stratified-wavy
Figure 5-14. Comparison of Van Dresar and Siegwarth data with the Wojtan et al. map.
intermittent regime data are predicted well, the annular regime data are not. This is likely
due to the low vapor quality encountered for annular flow during the chilldown process.
The modifications to Kattan et al. map only consider mass fluxes below 200 kg/m2-s;
thus the annular regime data lie outside the modified region, and the Kattan et al. map is
only valid for vapor qualities greater than 0.15.
Calibration of Taitel and Dukler Flow Regime Map
According to Taitel and Dukler [16], the transition between the stratified and the
intermittent or annular regimes is governed by the Kelvin-Helmholtz stability criterion
for wave propagation (Milne-Thompson [64]). Kordyban and Ranov [65] and Wallis and
Dobson [66] also utilized the Kelvin-Helmholtz stability criterion to analyze the
transition to slug flow. Lin and Hanratty [67] carried out a similar analysis and included
the viscous effects which were neglected in the earlier works, however no significant
69
Wavy Annular
= intermittent= annular= stratified-wavy
Slug
Plug
Bubbly
Dispersed
Figure 5-15. Comparison of current chilldown data with the Baker map.
10-2 10-1 100 101 10210-3
10-2
10-1
100
101
Annular Bubbly
Stratified-wavy
Intermittent
Stratified-smooth
= intermittent= annular= stratified-wavy
TF
K x 10-3
Xtt Figure 5-16. Comparison of current chilldown data with the Taitel and Dukler map.
70
Table 5-1. Sample data points for cryogenic chilldown. SW denotes stratified-wavy flow; I denotes intermittent flow; A denotes annular flow
Mass Flux kg/m2-s Quality
Saturation Temperature ºK
Flow Structure Observed
61 0.04 103.2 SW 60 0.04 103.0 SW 64 0.04 103.0 SW 72 0.03 103.3 SW 75 0.03 103.5 SW 74 0.03 103.9 SW 83 0.03 104.4 SW 84 0.03 104.7 SW 79 0.03 104.6 SW 80 0.03 104.6 SW 89 0.02 104.6 SW 86 0.02 104.4 SW 79 0.02 104.3 SW 390 0.03 90.8 I 399 0.03 91.3 I 394 0.03 90.5 I 355 0.04 90.7 I 376 0.06 90.5 I 366 0.04 89.8 I 351 0.05 90.0 I 346 0.04 90.0 I 336 0.03 90.0 I 378 0.06 90.0 I 330 0.04 89.9 I 273 0.04 89.1 I 291 0.06 88.9 I 295 0.08 89.1 I 323 0.03 89.2 I 301 0.06 89.2 I 502 0.13 97.6 A 583 0.10 97.7 A 600 0.06 96.9 A 569 0.08 96.2 A 603 0.04 96.3 A 612 0.11 96.1 A 575 0.09 95.6 A 588 0.12 95.5 A 606 0.07 94.6 A 572 0.07 94.8 A 537 0.17 95.3 A
71
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 10
100
200
300
400
500
600
Intermittent
Slug
Slug & Stratified-WavyStratified-smooth
Annular
Stratified-wavy
= intermittent= annular= stratified-wavy
G (k
g/m
2 s)
x Figure 5-17. Comparison of current chilldown data with the Wojtan et al. map.
difference was observed when compared to the work of Taitel and Dukler [16].
Taitel and Dukler [16] assumed a 2-D planar geometry with vapor flow on top of a
stationary liquid film with very large thickness compared to the size of any disturbances;
it was determined that the instability criterion takes the following form
( )12
1l g g
gg
gu C
ρ ρ δ
ρ
⎛ ⎞−⎜ ⎟>⎜ ⎟⎝ ⎠
, (5.1)
where 1C is a constant to be determined. A number of simplifying arguments were
presented to estimate a value of 1C that is less than unity. The analysis was extended to
an inclined pipe geometry to arrive at Eq. (2.5). The constant, 2C , in Eq. (2.5) is again
determined to be less than or equal to unity as revealed by Eq. (2.7). Here we consider
the stability analysis for a wave at the interface between the liquid and vapor phases in a
72
2-D planar configuration within a confined channel, with both fluids moving. The
configuration is illustrated in Fig. 5-18.
gδ
lδ
gu
luO
gρ
lρ
cx
y
Figure 5-18. Liquid-vapor 2-D channel flow configuration.
As determined by Milne-Thompson the equation that governs the wave speed is given by
( ) ( ) ( )22 coth coth .l l l g g g l gm u c m m u c m gρ δ ρ δ ρ ρ− + − = − (5.2)
Here m is the wave number, c is the wave speed, δ is the fluid height and all other
parameter are as define in the previous sections. The condition for stability dictates that
the wave speed, c , must be real. Equation (5.2) is a quadratic equation in c and thus can
be solved for c by utilizing the quadratic formula, hence we have
,2
42
AADBBc −±−
= (5.3)
here. A , B and D are constants given by Eq. (5.4),
coth cothl l g gA m m m mρ δ ρ δ= + (5.4a)
( )2 coth cothl l l g g gB u m m u m mρ δ ρ δ= − + (5.4b)
( )2 2coth coth .l l l g g g l gD m u m m u m gρ δ ρ δ ρ ρ= + − − (5.4c)
73
For the onset of wave instability the value of c must be imaginary thus we have the
condition,
.042 <− ADB (5.5)
After further simplification it is found that the Kelvin-Helmholtz instability is triggered
when
( )( )
11 122 2
12
1 1cosh cosh
l g gg lg
g g g l l gl g
guum m m m
g
ρ ρ δρδ ρ δ ρ δ ρ
ρ ρ
⎛ ⎞⎛ ⎞−⎛ ⎞ ⎛ ⎞⎜ ⎟⎜ ⎟> + +⎜ ⎟ ⎜ ⎟⎜ ⎟⎜ ⎟ ⎜ ⎟ ⎜ ⎟⎜ ⎟⎝ ⎠ ⎝ ⎠ ⎝ ⎠⎡ ⎤−⎣ ⎦⎝ ⎠
.(5.6)
Comparison of Eqs, (5.1) and (5.2) yield the following form for 1C ,
( )
1 12 2
1 12
1 1cosh cosh
g l
g g g l ll g
uCm m m m
g
ρδ ρ δ ρ δ
ρ ρ
⎛ ⎞⎛ ⎞ ⎛ ⎞⎜ ⎟
= + +⎜ ⎟ ⎜ ⎟⎜ ⎟⎜ ⎟ ⎜ ⎟⎜ ⎟⎝ ⎠ ⎝ ⎠⎡ ⎤−⎣ ⎦⎝ ⎠
. (5.7)
The value of 1C easily exceeds unity for small values of liquid film velocity and low and
moderate wave number. A liquid film velocity of 0.01m/s and wave number of yields a
value of 1C greater than 3, while a wave number of 1 gives a value of 1C greater than 10.
Hence it is expected that 2C in Eq. (2.5) may exceed unity for horizontal and inclined
pipe geometries.
In order to achieve better predictive capabilities, an attempt is made to calibrate the
Taitel and Dukler map. The transition boundary that demarcates the transition from
stratified-wavy to either annular or intermittent flow requires modification. As
previously discussed, the transition boundary depends on the value of the constant 2C .
For the present data a better fitting transition boundary is obtained when the functional
form of 2C is calibrated so as to best fit the data. The calibrated value of 2C is given by
74
12 2
-22 0.72
tt
1.494.516X
C
−−⎡ ⎤⎛ ⎞
⎢ ⎥= + ⎜ ⎟⎢ ⎥⎝ ⎠⎣ ⎦
. (5.8)
Hence 2C ranges from 0 to 4.516. This is consistent with Eq. (5.6). The
demarcation line for the transition between the annular and the intermittent flow regimes
must also be shifted to the right; this transition line was set based on the assumption that
intermittent flow can only be present if the height of the liquid film is greater than the
pipe radius, which may not necessarily be correct. The transition boundary between the
annular and intermittent flow regimes is shifted from 1.6ttX = to 4.0ttX = , which
represents a small change physically. Instead of transition to intermittent flow if the
liquid film height is greater than the radius of the pipe, the shift corresponds to transition
to intermittent flow if the liquid film height greater than 0.55D . The resulting flow map
is compared with the chilldown data and is presented in Fig. 5-19. The flow regime
transitions are significantly improved with the calibration to the Taitel and Dukler [16]
flow regime map.
The annular flow regime is typically characterized by thin liquid films with
moderate velocities. The oversimplified assumptions used by Taitel and Dukler [16] to
arrive at Eq. (5.1) severely limits the parameter space for which their flow regime
transition from stratified to annular flow or intermittent flow is valid. Indeed, Eq. (5.6)
shows that the liquid height and liquid velocity can play an important role in Kelvin-
Helmholtz instability. The experimentally observed stratified to annular flow regime
transitions in this work clearly support the notion that the liquid film height and liquid
velocity are important parameters in the flow regime transition.
75
10-2 10-1 100 101 10210-3
10-2
10-1
100
101
AnnularBubbly
Stratified-smooth
T
F
K x 10-3
Xtt
Stratified-wavy
= intermittent= annular= stratified-wavy
Intermittent
Figure 5-19. Comparison of current chilldown data with the modified Taitel and Dukler
map.
Film Boiling Heat Transfer
This section focuses on measuring the heat transfer coefficients associated with the
complex, unsteady, film flow boiling heat transfer that occurs during cryogenic
chilldown; the prediction and modeling of the film boiling heat transfer coefficients is
currently under investigation by a fellow graduate student. The inverse technique
described in chapter 4 is used to extract the heat transfer coefficient from time dependent
measurements of wall temperature. Using knowledge of the local temperature of the
pipeline coupled with numerical simulations of the unsteady heat conduction through the
wall of the pipe to determine the heat transfer coefficients.
Figures 5-20 and 5-21 show the film boiling heat transfer coefficients extracted
from the experimental data of the low (75 kg/m2s) and moderate mass flux (210 kg/m2s)
76
experiments highlighted at the beginning of the chapter, respectively. It is observed from
both Figs.5-20 and 5-21 that the heat transfer coefficient in the lower portion of the pipe
(region 3) is at least double in magnitude to the heat transfer coefficient in the other two
regions. This is as expected since the liquid film resides in the lower region of the pipe
and due to gravitational effects the vapor film that separates the liquid film from the pipe
wall is thinnest at the bottom. By comparing Fig. 5-20 to 5-21 it is seen that the higher
the mass flux the larger the heat transfer coefficient. This is also as expected since
convective heat transfer increases with increasing mass flux. It is interesting to note that
for the low mass flux experiment it is observed that the heat transfer coefficient at the
side of the pipe (region 2) is slightly smaller than the heat transfer coefficient at the top of
the pipe (region 1). This trend was observed for experiment where the average mass flux
was below 120 kg/m2s, in experiments. One possible reason for this is that the
circumferential conduction heat to the lower region (region 3) is larger for lower mass
fluxes, since the convective heat transfer is reduced.
The heat transfer coefficients for the film boiling regime are available in tabulated
form in appendix B.
Nucleate Flow Boiling Heat Transfer
This section focuses on measuring and predicting the heat transfer rates associated
with the complex, unsteady, nucleate flow boiling heat transfer that occurs during
cryogenic chilldown. The inverse technique described in chapter 4 is used to extract the
heat transfer coefficient from time dependent measurements of wall temperature. This
technique utilizes knowledge of the local temperature of the pipeline coupled with
numerical simulations of the unsteady heat transfer through the wall of the pipeline to
77
determine the heat transfer coefficients. These experimentally determined heat transfer
coefficients are compared against the nucleate flow boiling heat transfer correlations
0
100
200
300
400
500
600
0 10 20 30 40 50 60 70 80 90Time (sec.)
Hea
t Tra
nsfe
r Coe
ffici
ent (
W/m
2 K)
Region 1 (Top)Region 2 (Side)Region 3 (Bottom)
275G kg m s=
Figure 5-20. Heat transfer coefficients for each region in the film boiling regime of the
low mass flux experiment.
0
100
200
300
400
500
600
0 5 10 15 20 25 30 35 40 45Time (sec.)
Hea
t Tra
nsfe
r Coe
ffici
ent (
W/m
2 K)
Region 1 (Top)Region 2 (Side)Region 3 (Bottom)
2210G kg m s=
Figure 5-21. Heat transfer coefficients for each region in the film boiling regime of the
moderate mass flux experiment.
78
of Gungor and Winterton [30], Kandlikar [40], Müller-Steinhagen and Jamialahmadi [33]
and Thome [43].
Performance of Current Flow Boiling Heat Transfer Correlations
In determining the heat transfer coefficients using the inverse procedure outlined in
chapter 4, it is sometimes necessary to change the size of the various regions. In order to
compare the results obtained to existing correlations, an average heat transfer coefficient
must be computed. This is done by integrating the heat transfer coefficients assigned on
the inner surface over the perimeter of the inner surface. This approach is also employed
by Thome [43]. Hence the average two-phase heat transfer coefficient, 2h φ , is computed
as
( ) ( )2 1 212 .top side bottomh h h hφ
α α π ααπ π π
− −= + + (5.9)
Fig. 5-22 illustrates the variation of the average two-phase heat transfer coefficient
extracted from the experimental data with time for the chilldown process. It is clearly
seen that the transition from the film boiling regime to the nucleate flow boiling regime is
accompanied by an order of magnitude increase in the average two-phase heat transfer
coefficient. The robust nature of the computational method is demonstrated in that it is
able to handle the step change in heat transfer coefficient from the film to nucleate
boiling regime.
The nucleate flow boiling heat transfer coefficients extracted from the experimental
data are presented in Table 5-3. The mass flux, vapor quality, flow regime, and
saturation temperature are shown. In addition, the fraction of the perimeter occupied by
each region, the average wall temperature, and the contribution to the two-phase heat
transfer in each region are tabulated. It is observed that the influence of region 1 on the
79
average two-phase heat transfer coefficient in the nucleate flow boiling regime is small
when compared to the influence of regions 2 and 3.
0
500
1000
1500
2000
2500
3000
3500
0 10 20 30 40 50 60Time (sec.)
Hea
t Tra
nsfe
r Coe
ffic
ient
(W/m
2 K)
2102 , 239satkgT K Gm s
= =
Nucleate Boiling Regime
Film Boiling Regime
Figure 5-22. Average two-phase heat transfer coefficient variation with time.
This is as a result of the stratified nature for the flow structure, in which the liquid
resides in the lower regions of the pipe while the vapor resides in the upper region. By
examining the contributions from each region to the total heat transfer, it is observed that
in some instances region 2 has a larger contribution than region 3. This occurs because
of the unsteady nature of the flow which results in instances where region 2 is
periodically wetted resulting in a thinner liquid film than in region 3. Hence the heat
transfer rate in region 2 will be greater as a result of the lower thermal resistance of the
liquid film.
In examining the fraction of the area assigned to each region it is evident that the
flow structure influences the size of each region. For annular flow and stratified-wavy
80
flow in which the liquid film height is greater than the radius of the pipe, the three
regions may be constructed such that they are of equal size. While in the intermittent
flow regime the size of each region is adjusted slightly. However, when the flow is in the
stratified-wavy regime, a significant difference in the size of regions is observed. This
results from the inability to determine the actual wetted area of the pipe. If the size of
region 3 is overestimated the energy removed from the pipe wall would be too large in
the adjacent region (in this case region 2) making it impossible to match the outer wall
temperature. This problem is encountered mainly in the stratified-wavy regime, in which
the height of the liquid film is less than the pipe radius. It is not encountered with the
other flow structures since the wetted area is not overestimated. Provided the wetted
region is not overestimated, the size of regions 1, 2 and 3 may have different values, and
yet suitable agreement with measured data is found. Therefore, the solution presented is
not unique. Nevertheless, it is found that the average heat transfer coefficient hardly
changes with variations in the size of regions 1, 2, and 3.
In order to maintain consistency, these regions were taken to be of equal size, unless the
solution required differently. For this work the regions sizes were chosen to maintain as
much symmetry as possible while ensuring that the size of the wetted region is not
overestimated. The database of cryogenic nucleate flow boiling heat transfer coefficient
for chilldown presented in Table 5-3 is the only one we are aware of.
In Table 5-3, SW (0.5+) denotes stratified wavy flow where the height of the liquid film
greater than 2id ; I denotes intermittent flow; SW (0.5-) denotes stratified wavy flow
where the height of the liquid film less than 2id ; A denotes annular flow.
81
Table 5-3. Summary of measured average nucleate flow boiling heat transfer coefficients using inverse method for regions.
Flow Regime
Mass Flux x Sat.
Temp.
Fraction of area & Avg. Wall Temp
for Region 1
Fraction of area & Avg.
Wall Temp for Region 2
Fraction of area & Avg. Wall Temp
for Region 3
tph
kg/m2s ºK πα1 ºK π
αα 12 − ºK παπ 2− ºK W/m2
K
SW (0.5+) 61 0.04 103.2 0.33 151.5 0.33 131.0 0.33 105.3 2203 SW (0.5+) 60 0.04 103.0 0.33 153.8 0.33 130.8 0.33 109.4 1561 SW (0.5+) 64 0.04 103.0 0.33 151.2 0.33 125.2 0.33 110.1 1852 SW (0.5+) 72 0.03 103.3 0.33 156.8 0.33 141.8 0.33 116.0 1265 SW (0.5+) 75 0.03 103.5 0.33 155.2 0.33 136.6 0.33 106.9 2211 SW (0.5+) 74 0.03 103.9 0.33 152.9 0.33 131.0 0.33 107.8 2508 SW (0.5+) 83 0.03 104.4 0.33 151.0 0.33 127.3 0.33 112.1 1881 SW (0.5+) 84 0.03 104.7 0.33 145.3 0.33 111.5 0.33 108.8 2888 SW (0.5+) 79 0.03 104.6 0.33 139.6 0.33 111.2 0.33 108.2 2787 SW (0.5+) 80 0.03 104.6 0.33 134.2 0.33 110.0 0.33 107.1 2429 SW (0.5+) 89 0.02 104.6 0.33 138.9 0.33 122.6 0.33 107.8 1514 SW (0.5+) 86 0.02 104.4 0.33 135.3 0.33 107.7 0.33 102.2 2374 SW (0.5+) 79 0.02 104.3 0.33 132.6 0.33 105.3 0.33 103.2 1588 SW (0.5+) 390 0.03 90.8 0.33 145.6 0.33 122.9 0.33 108.1 1967 SW (0.5+) 399 0.03 91.3 0.33 142.0 0.33 111.4 0.33 107.5 2381
I 394 0.03 90.5 0.42 126.7 0.29 99.4 0.29 100.3 1790 I 355 0.04 90.7 0.42 152.1 0.29 131.6 0.29 115.1 1300 I 376 0.06 90.5 0.42 148.6 0.29 118.1 0.29 111.3 1880 I 366 0.04 89.8 0.42 145.7 0.29 113.8 0.29 111.6 1554 I 351 0.05 90.0 0.42 142.9 0.29 113.1 0.29 110.6 1345 I 346 0.04 90.0 0.42 140.1 0.29 112.3 0.29 108.4 1631 I 336 0.03 90.0 0.42 137.2 0.29 110.1 0.29 108.0 1932
SW (0.5-) 378 0.06 90.0 0.42 121.0 0.42 107.2 0.16 93.1 1247 SW (0.5-) 330 0.04 89.9 0.42 119.5 0.42 93.0 0.16 90.2 5097 SW (0.5-) 273 0.04 89.1 0.42 117.9 0.42 101.0 0.16 89.2 1848 SW (0.5-) 291 0.06 88.9 0.42 124.3 0.42 110.6 0.16 97.5 1103 SW (0.5-) 295 0.08 89.1 0.42 118.6 0.42 91.8 0.16 92.8 2255 SW (0.5-) 323 0.03 89.2 0.42 120.2 0.42 100.9 0.16 94.6 2103 SW (0.5-) 301 0.06 89.2 0.42 118.1 0.42 105.4 0.16 97.2 1330 SW (0.5-) 502 0.13 97.6 0.42 115.4 0.42 90.4 0.16 94.4 3806 SW (0.5-) 583 0.10 97.7 0.42 115.5 0.42 99.4 0.16 96.3 1904 SW (0.5-) 600 0.06 96.9 0.42 119.7 0.42 96.4 0.16 96.0 2264 SW (0.5-) 569 0.08 96.2 0.42 119.1 0.42 97.2 0.16 96.0 2218 SW (0.5-) 603 0.04 96.3 0.42 140.1 0.42 120.5 0.16 101.3 1342 SW (0.5-) 612 0.11 96.1 0.42 138.9 0.42 114.7 0.16 103.7 1081 SW (0.5-) 575 0.09 95.6 0.42 124.0 0.42 107.1 0.16 105.5 1706
A 588 0.12 95.5 0.33 130.8 0.33 114.7 0.33 108.4 1654 A 606 0.07 94.6 0.33 128.3 0.33 104.8 0.33 104.4 2149 A 572 0.07 94.8 0.33 127.3 0.33 110.4 0.33 104.6 2225 A 537 0.17 95.3 0.33 124.9 0.33 104.7 0.33 106.0 2203 A 352 0.039 95.2 0.33 127.4 0.33 111.2 0.33 106.5 1682 A 415 0.053 95.0 0.33 124.9 0.33 104.0 0.33 105.7 1808
82
Comparisons of the computed average flow boiling heat transfer coefficients with
those determined experimentally are shown in Figs 5-23, 5-24, 5-25 and 5-26. Figs 5-23,
5-24, 5-25 and 5-26 show comparisons with the Gungor and Winterton, Kandlikar,
Müller-Steinhagen and Jamialahmadi, and Thome correlations, respectively. It is
observed that the Müller-Steinhagen and Jamialahmadi correlation performs the best,
predicting 47.6% of the data within the 25% error band. This is followed by the Gungor
and Winterton correlation with 38.1%, then the Thome correlation with 21.4% and finally
the Kandlikar carrleation with 9.5%.
The Kandlikar correlation and Gungor and Winterton correlation both over predict
the heat transfer coefficient. Thus in applying these correlations care must be taken in
order to account for the region that is actually wetted during the flow boiling process.
The Thome correlation under predicts the heat transfer coefficient. Although this
correlation is the only one tested that takes into account the flow structure, it has not been
extensively tested within the low quality range encountered during the chilldown
experiments. The Müller-Steinhagen and Jamialahmadi perfoms the best for the present
data, however this correlation does not account for the flow structure. This information
gives a reasonable starting point for the development of a reliable correlation for nucleate
flow boiling during cryogenic chilldown.
Correlating the Nucleate Flow Boiling Heat Transfer Coefficient
Many of the current flow boiling heat transfer coefficient correlations ignore the
flow structure in their predictions. Of the correlations considered here only the
correlation of Thome [43] takes in to account the structure of the flow, however it is seen
from Fig. 5-26 that this particular correlation under-predicts the data. Since the
83
0.00
1000.00
2000.00
3000.00
4000.00
5000.00
6000.00
0 1000 2000 3000 4000 5000 6000
Measured Heat Transfer Coefficient (W/m2K)
Pred
icte
d H
eat T
rans
fer C
oeffi
cien
t(W
/m2 K
)
+25%
-25%
Figure 5-23. Comparison of predicted and measured average nucleate flow boiling heat
transfer coefficients using Gungor and Winterton correlation.
0
1000
2000
3000
4000
5000
6000
0 1000 2000 3000 4000 5000 6000
Measured Heat Transfer Coefficient (W/m2K)
Pred
icte
d H
eat T
rans
fer C
oeffi
cien
t (W
/m2 K
)
+25%
-25%
Figure 5-24. Comparison of predicted and measured average nucleate flow boiling heat
transfer coefficients using Kandlikar correlation.
84
0.00
1000.00
2000.00
3000.00
4000.00
5000.00
6000.00
0 1000 2000 3000 4000 5000 6000
Measured Heat Transfer Coefficient (W/m2K)
Pred
icte
d H
eat T
rans
fer
Coe
ffic
ient
(W
/m2 K
)
+25%
-25%
Figure 5-25. Comparison of predicted and measured average nucleate flow boiling heat
transfer coefficients using Müller-Steinhagen correlation.
0
1000
2000
3000
4000
5000
6000
0 1000 2000 3000 4000 5000 6000
Measured Heat Transfer Coefficient (W/m2K)
Pred
icte
d H
eat T
rans
fer C
oeffi
cien
t (W
/m2 K
)
+25%
-25%
Figure 5-26. Comparison of predicted and measured average nucleate flow boiling heat
transfer coefficients using Wojtan et al. correlation.
Müller-Steinhagen and Jamialahmadi correlation performs best for the average heat
transfer coefficient it is proposed that a better result may be obtained by applying a single
85
phase convective correlation for the dry perimeter of the pipe. Here the case the Dittus-
Boelter correlation is used. The Müller-Steinhagen and Jamialahmadi correlation is used
for the wetted perimeter of the pipe. This is shown pictorially in Fig. 5-27.
Liquid Phase
Vapor Phase
Dittus-Boeltercorrelationfor single phasevapor
Muller-Steinhagenand Jamoalahmadicorrelation for flowboiling in liquid phase
Figure 5-27. Method for assigning the heat transfer coefficient on the inside surface of
the pipe.
In order to assess the effectiveness of this approach, the outer wall temperatures
will be computed using this approach of assigning the heat transfer coefficient on the
inner surface of the pipe, in the nucleate boiling regime. The wetted area is determined
using the measured liquid heights from the digital images of the flow structure. Once the
temperatures are computed they are then compared to the measured wall temperatures at
the corresponding time instance.
It was observed that the temperature values predicted for the dry region of the pipe,
i.e. the region that is in contact with the vapor, agree well with the measured
temperatures. However, the temperatures predicted at the side and at the bottom of the
pipe do not match well with the measured temperatures in those locations. In examining
the Müller-Steinhagen and Jamialahmadi correlation, it is seen that the enhancement of
86
the convective contribution to the heat transfer correlation does not account for the heat
flux into the system. The correlation of Gungor and Winterton [30] incorporates the
effect of the heat flux in the convective term by including a Boiling number, Bo , term, as
expressed in Eq. (2.23). The Boiling number is defined in Eq. (2.21). Following the lead
of Gungor and Winterton [30], the effect of the heat flux is incorporated through the use
of the Boiling number in the enhancement factor for the convective term of the heat
transfer coefficient. Thus the modified correlation for the nucleate flow boiling heat
transfer coefficient applied to the wetted perimeter takes the form
2 .l nbh Eh Shφ = + (5.10)
Here lh is defined in Eq. (2.29), nbh is defined in Eq (2.32), S is defined in Eq. (2.19)
and the enhancement factor, E is given by
0.863 1.29 11 5 10 1.37
1.5 tt
E BoX
⎛ ⎞= + × + ⎜ ⎟
⎝ ⎠ (5.11)
where Bo is defined in Eq. (2.21), and the Martinelli parameter, ttX , is given in Eq.
(2.12).
Employing this modified correlation significantly improves the prediction of the
temperature at the bottom of the pipe wall. This is illustrated in Figs. 5-28 to 5-46, which
compare the predicted outer wall temperatures to the measured outer wall temperatures
with the original Müller-Steinhagen and Jamialahmadi correlation and the modified
version. It is of interest to note that the temperature on the side is not well predicted
using either correlation in the wetted region. The primary reason for this is the inability
to accurately determine the actual area that is wetted by the liquid phase in the side wall
87
region. Periodic liquid wetting results in very high heat transfer coefficients, and such
behavior is not accounted for using this simple model.
-180
-170
-160
-150
-140
-130
-120
58.8 59 59.2 59.4 59.6 59.8 60 60.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-28. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 140 kg/m2s.
-180
-170
-160
-150
-140
-130
-120
86.8 87 87.2 87.4 87.6 87.8 88 88.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-29. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 76 kg/m2s.
88
-180
-170
-160
-150
-140
-130
-120
104.8 105 105.2 105.4 105.6 105.8 106 106.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-30. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 62 kg/m2s.
-180
-170
-160
-150
-140
-130
-120
40.5 41 41.5 42 42.5 43 43.5Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-31. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 211 kg/m2s.
89
-180
-170
-160
-150
-140
-130
45.5 46 46.5 47 47.5 48 48.5Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-32. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 292 kg/m2s.
-180
-170
-160
-150
-140
-130
-120
47.8 48 48.2 48.4 48.6 48.8 49 49.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-33. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 279 kg/m2s.
90
-180
-170
-160
-150
-140
-130
-120
61.8 62 62.2 62.4 62.6 62.8 63 63.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-34. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 210 kg/m2s.
-180
-170
-160
-150
-140
-130
-120
83.5 84 84.5 85 85.5 86 86.5 87 87.5 88 88.5Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-35. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 186 kg/m2s.
91
-190
-180
-170
-160
-150
120.8 121 121.2 121.4 121.6 121.8 122 122.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-36. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 95 kg/m2s.
-190
-180
-170
-160
-150
108.8 109 109.2 109.4 109.6 109.8 110 110.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-37. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 113 kg/m2s.
92
-190
-180
-170
-160
-150
86.8 87 87.2 87.4 87.6 87.8 88 88.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-38. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 93 kg/m2s.
-190
-180
-170
-160
-150
135.8 136 136.2 136.4 136.6 136.8 137 137.2Time (sec.)
Tem
pera
ture
(o C) Top: Measured
Side: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-39. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 134 kg/m2s.
93
-190
-180
-170
-160
-150
105.8 106 106.2 106.4 106.6 106.8 107 107.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-40. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 127 kg/m2s.
-190
-180
-170
-160
-150
105.8 106 106.2 106.4 106.6 106.8 107 107.2
Time (sec.)
Tem
pera
ture
(o C) Top: Measured
Side: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-41. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 132 kg/m2s.
94
-190
-180
-170
-160
-150
92.8 93 93.2 93.4 93.6 93.8 94 94.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-42. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 162 kg/m2s.
-185
-175
-165
-155
68.8 69 69.2 69.4 69.6 69.8 70 70.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-43. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 165 kg/m2s.
95
-190
-180
-170
-160
-150
87.8 88 88.2 88.4 88.6 88.8 89 89.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-44. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 153 kg/m2s.
-180
-170
-160
-150
-140
-130
132.8 133 133.2 133.4 133.6 133.8 134 134.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-45 Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 94 kg/m2s.
96
-180
-170
-160
-150
-140
-130
114.8 115 115.2 115.4 115.6 115.8 116 116.2Time (sec.)
Tem
pera
ture
(o C)
Top: MeasuredSide: MeasuredBottom: MeasuredTop: Muller-SteinhagenSide: Muller-SteinhagenBottom: Muller-SteinhagenTop: Modified with Bo NumberSide: Modified with Bo NumberBottom: Modified with Bo Number
Figure 5-46. Comparison of the predicted and measured temperatures using both the
Müller-Steinhagen and Jamialahmadi correlation and the modified version. Average mass flux 94 kg/m2s.
In order to better compare the performance of this modified version of the Müller-
Steinhagen and Jamialahmadi correlation, the predicted average heat transfer coefficient
is computed and then compared to the measured average heat transfer coefficient. The
results are shown in Fig. 5-47. It is seen from Fig. 5-47 that the prediction of the average
heat transfer coefficient is significantly improved, with 75.6% of the data lying within the
25% error band. This clearly demonstrates that the Boiling number is an important
parameter when considering the enhancement of the convective contribution to the heat
transfer coefficient.
This observation is consistent with the findings of Klausner [60], who observed that
at with increasing heat fluxes, the two-phase friction pressure drop increases in horizontal
flows compared with adiabatic flow at the same vapor quality and vapor volume fraction.
This suggests that the bulk turbulent convection increases as a result of increasing
97
0
1000
2000
3000
4000
5000
6000
0 1000 2000 3000 4000 5000 6000
Measured Heat Transfer Coefficient (W/m2K)
Pred
icte
d H
eat T
rans
fer
Coe
ffic
ient
(W/m
2 K) +25
-25
Figure 5-47. Comparison of predicted and measured average nucleate flow boiling heat
transfer coefficients using modified Müller-Steinhagen and Jamialahmadi correlation.
transverse vapor momentum at higher heat fluxes. In the current work, the local heat
fluxes are seen to range from 10.4 kW/m2 to 103.6 kW/m2, which are consistent with the
heat flux ranges investigated by Klausner [60].
98
CHAPTER 6 CONCLUSIONS AND RECOMMENDATIONS FOR FUTURE RESEARCH
The process of cryogenic chilldown is very complex and although attempts have
been made to simulate the momentum and energy interactions, prior attempts have been
fair at best. One of the major reasons is the lack of reliable data and correlations that
encompass the parameter space associated with cryogenic fluids. This work has taken the
much needed first step in compiling a database of flow structures, mass flow rates,
pressure drop and heat transfer coefficients in both the film boiling and nucleate boiling
regimes.
In order to extract the unsteady heat transfer coefficients from the experimental
temperature data, a novel inverse approach has been developed that utilizes finite volume
computations to deduce the heat transfer coefficients based on the measured
temperatures. The technique assumes a given heat transfer coefficient on the inner
surface of the pipe and computes the unsteady temperature field within the pipe wall then
checks whether the computed temperature field matches the measured temperature values
at specified locations. If a match is achieved then the assumed heat transfer coefficient is
considered to be the actual heat transfer coefficient at that location. If a match is not
obtained a different heat transfer coefficient is assumed and the process is repeated until a
match is obtained.
The inverse technique is seen to perform well for single phase flow structures;
however, for two-phase flow structures a suitable approach must be employed to account
for circumferential variations in the heat transfer coefficient. This work uses a simple
99
model that divides the inner perimeter into three regions, and the heat transfer coefficient
is assumed constant in each region. The actual variation of the heat transfer coefficient is
more complicated, although the approach used proved to be adequate and robust. This is
one of the areas where further work is required. Better models are desired to account for
the circumferential variations of the heat transfer coefficient. As a result more detailed
studies must be conducted to gain a better understanding of the fluid interaction with the
wall, as these interactions greatly affect the magnitude of the heat transfer rates,
especially in the nucleate flow boiling regime.
The experimental data gathered were used to calibrate existing models for
predicting flow regime transitions and the nucleate flow boiling heat transfer coefficients.
It was highlighted that even though the Taitel and Dukler [16] flow regime map is the
map best suited to predict chilldown flow regime transitions, it utilizes assumptions that
oversimplify the transition boundary between the stratified-wavy and the
intermittent/annular regimes. The transition was calibrated to give a significantly better
performance. For future studies, a more mechanistic approach for modifying the
transition boundary is desired so that the modified map may be applied to a wider range
of operating parameters and operating fluids.
The flow boiling heat transfer correlation of Müller-Steinhagen and Jamialahmadi
[39] performs best of the correlations tested here, but it lacks two major features
necessary for it to be utilized for correlating the flow boiling heat transfer coefficient in
cryogenic chilldown. The most obvious shortcoming is that it ignores the flow structure,
which plays a major role in determining the heat transfer. Secondly, it ignores the
influence of local heat flux on the enhancement of the convective component of the heat
100
transfer coefficient. A simple model that includes the effect of flow structure and the
enhancement provided by the local heat flux, significantly improves the predictive
capabilities of the correlation. To achieve even better performance detailed knowledge of
the wetting phenomena on the inner surface of the pipe must be known. This is another
area that requires further work.
This work has provided a database that will aid in the development and
improvement of models and correlations that are useful to predict the thermal hydraulic
transport for the chilldown process. A useful inverse technique for extracting the
unsteady heat transfer coefficients in both the film and the nucleate boiling regimes has
been developed. A modified Taitel and Dukler map is given that is applicable to
cryogenic chilldown with liquid nitrogen. And a flow boiling heat transfer correlation is
proposed that gives better performance than those currently available.
101
APPENDIX A PHYSICAL PROPERTIES OF NITROGEN
The physical properties for nitrogen may be obtained by utilizing the following
curve fit equations:
T is in °C.
ρl = -0.202330 x 104 - 0.251212 x 102 *T - 0.546161 x 10-1 * T2 (kg/m3)
ρv = 0.925489 x 101 - 0.859076 x 10-1 *T - 0.454727 x 10-3 * T2 (kg/m3)
µl = -0.954068 x 10-4 - 0.103000 x 10-5 * T + 0.678184 x 10-8 * T2
+ 0.642683 x 10-10 * T3 - 0.229346 x 10-12*T4 - 0.211157 x 10-14*T5 (Ns/m2)
µv = 0.607870 x 10-4 + 0.509473 x 10-6 * T + 0.116164 x 10-8 * T2 (Ns/m2)
cpl = 2.2956 x 104 + 1.49146 x 10*T - 0.602354 * T2
+ 0.289989 x 10-2 * T3 -0.166225 x 10-4 * T4 - 0.704924 x 10-6 * T5
+ 0.115665 x 10-8 * T6-0.125146 x 10-11 * T7-0.222653 x 10-13*T8 (kJ/kgK)
cpv = 0.44248 x 1014*EXP(0.253474 * T + 0.659959 x10-3 * T2) (kJ/kgK)
102
kl = -0.135374 - 0.879867 x10-3 * T + 0.242658 x 10-5 *T2
- 0.207528 x 10-8 *T3 (W/mK)
kv = 0.140406 + 0.79933 x 10-4 * T -0 .36289 x 10-5 * T2 + 0.18728 x 10-7 * T3
-0.99885 x 10-10 * T4 - 0.407198 x 10-12 * T5 +7 .02725 x 10-15 * T6
-7.14345 x 10-18 * T7- 1.31179 x 10-19 * T8 (W/mK)
hf = 6.62495 x 105 + 6.13878 x 103 * T+ 1.09164 x 10 * T2 (J/kg)
hg = -1.74503 x x105 – 7.49609 x 102 *T + 4.93291 * T2-0.113927 x 10-1 * T3
+0.299316 x 10-3 * T4+0.360372 x 10-7 * T5-0.172519 x 10-7 * T6
+0.238447 x 10-10 * T7+0.29486x 10-12 * T8 (J/kg)
hfg = hg-hf (J/kg)
Psat = 0.380945 x 102 + 0.310646 * T + 0.177896 x 10-3 * T2
- 0.214602 x10-5 * T3 (MPa)
σ = -0.488624 x 10-2 + 0.398741 x 10-4 * T + 0.160255 x 10-6 * T2
-0.203075.179123E-13 x10-8 * T3 + 0.365340 x 10-11 * T4
+ 0.179123E x 10-13 * T5 (N/m)
103
APPENDIX B EXPERIMENTAL DATABASE: FLOW REGIME, HEAT TRANSFER
COEFFICIENT, AND PRESSURE DROP DURING CHILLDOWN
A1 fraction of inner pipe perimeter occupied by region 1
A2 fraction of inner pipe perimeter occupied by region 2
A3 fraction of inner pipe perimeter occupied by region 3
FR flow regime
G mass flux (kg/m2s)
h1 heat transfer coefficient extracted from region 1 (W/m2K)
h2 heat transfer coefficient extracted from region 2 (W/m2K)
h3 heat transfer coefficient extracted from region 3 (W/m2K)
∆P pressure drop across visual test section (kPa)
Tsat saturation temperature (ºC)
Tw,b outer wall temperature measured at the bottom of the pipe (ºC)
Tw,i inner wall temperature in respective region (ºC)
Tw,s outer wall temperature measured at the side of the pipe(ºC)
Tw,t outer wall temperature measured at the top of the pipe(ºC)
t time (s)
x vapor quality
δ liquid film height (mm)
δb liquid film thickness at the bottom of the pipe in annular
flow (mm)
δt liquid film thickness at the top of the pipe in annular flow (mm)
104
EXP 1 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 73 1 -29.4 0.333 19 21 328 0.333 18.2 21.1 363 0.333 17.4 19.7 431.7 0.0 1 S 89.7 0.295 -72.2 0.333 17.1 18.3 146.1 0.333 16.1 18.3 141.9 0.333 13.4 15.1 288.5 1.6 2 S 100.5 0.248 -97.1 0.333 14.1 15.4 164.8 0.333 12.6 14.9 165 0.333 7.9 9.5 338.6 1.8 3 S 102.8 0.229 -109.6 0.333 11 12.2 166 0.333 8.7 11.2 175.7 0.333 2.2 3.4 364.5 1.8 4 N 108.2 0.201 -116 0.333 8 9.2 154.2 0.333 4.7 7.2 172.7 0.333 -3.8 -2.9 385.8 0.0 5 S 108.8 0.192 -122.8 0.333 5.1 6.2 110.7 0.333 0.7 3.1 126.3 0.333 -9.4 -9.1 289.3 1.1 6 S 118 0.168 -168.3 0.333 2 3.1 110.8 0.333 -3.4 -1.3 132.6 0.333 -14.5 -14.7 265.7 1.4 7 S 123.5 0.161 -176 0.333 -1.4 -0.2 121.5 0.333 -7.6 -5.7 138 0.333 -19.1 -19.8 251.9 1.7 8 N 113.4 0.157 -175.7 0.333 -4.6 -3.5 116.2 0.333 -11.7 -9.9 135.2 0.333 -24.3 -25.1 280.5 0.0 9 S 127.8 0.132 -175.7 0.333 -7.6 -6.6 110.1 0.333 -15.3 -13.8 119.8 0.333 -29.1 -30.3 281.8 1.9 10 S 117.8 0.149 -175.7 0.333 -10.5 -9.7 106.4 0.333 -18.8 -17.3 114.4 0.333 -33.1 -34.8 257.2 1.6 11 N 124.2 0.118 -175.9 0.333 -13.3 -12.5 99.1 0.333 -22.4 -21 118.3 0.333 -37.4 -39.3 276.2 0.0 12 S 120.5 0.134 -174.9 0.333 -16.4 -15.6 110.1 0.333 -25.6 -24.6 102.1 0.333 -41.4 -43.7 274.2 1.9 13 N 129.6 0.106 -175.6 0.333 -19.2 -18.6 104.5 0.333 -28.9 -28.1 108.5 0.333 -45 -47.6 263.6 0.0 14 S 132.8 0.117 -174.5 0.333 -22.3 -21.7 113.2 0.333 -32.1 -31.5 103.5 0.333 -48.8 -51.6 279.9 1.8 15 N 132 0.103 -175.1 0.333 -25 -24.6 101.1 0.333 -35.3 -34.9 106.2 0.333 -52.4 -55.4 276.7 0.0 16 S 125.5 0.109 -174.3 0.333 -27.9 -27.6 111.2 0.333 -38.5 -38.3 102.5 0.333 -56 -59.2 285.2 4.1 17 S 134.2 0.093 -175.1 0.333 -30.8 -30.6 109.2 0.333 -41.7 -41.6 110.7 0.333 -59.2 -62.6 274.3 2.1 18 N 126.9 0.103 -173.8 0.333 -34 -33.8 120.9 0.333 -45.1 -44.9 116.6 0.333 -62.7 -66.1 291.1 0.0 19 S 129.8 0.091 -174.6 0.333 -36.8 -36.8 113.6 0.333 -48.1 -48.1 113.3 0.333 -65.2 -69 255.4 2.5 20 S 119.4 0.098 -173.7 0.333 -40.1 -40.1 128.4 0.333 -51.5 -51.4 129.9 0.333 -68.5 -72.2 283.6 1.9 21 N 130.6 0.084 -174.5 0.333 -42.9 -43.1 116.1 0.333 -54.5 -54.5 123.4 0.333 -71.1 -74.9 259.4 0.0 22 S 113.1 0.096 -173.5 0.333 -45.8 -46.2 119.4 0.333 -57.3 -57.5 108.2 0.333 -73.9 -77.7 273.5 2.5 23 S 129.7 0.077 -174.2 0.333 -48.4 -49 109.5 0.333 -60.1 -60.3 112.6 0.333 -76.7 -80.6 280.2 2.1 24 N 136.6 0.082 -173.5 0.333 -51.2 -51.9 120.9 0.333 -62.6 -63.1 98.1 0.333 -79.1 -83.2 266.7 0.0 25 S 130.3 0.082 -173.4 0.333 -53.7 -54.6 107.4 0.333 -65.2 -65.9 97.5 0.333 -82.2 -86.2 308.2 3.3 26 S 148.1 0.075 -174.2 0.333 -56.4 -57.5 118.4 0.333 -67.8 -68.6 106.7 0.333 -84.3 -88.5 260.4 3.3 27 S 124.6 0.087 -173 0.333 -59.2 -60.3 124.4 0.333 -70.9 -71.6 128.7 0.333 -87.5 -91.5 321.2 4.3 28 S 150.7 0.071 -174 0.333 -61.7 -63 113.5 0.333 -73.5 -74.2 115.2 0.333 -89.8 -94.1 290.6 2.0 29 S 146.8 0.075 -173.1 0.333 -64.3 -65.8 124 0.333 -75.9 -76.9 108 0.333 -92 -96.3 280.8 1.5 30 S 130.6 0.076 -173 0.333 -66.7 -68.4 113.8 0.333 -78.5 -79.4 111.3 0.333 -94.9 -99.1 326.8 1.5 31 S 145.3 0.068 -174 0.333 -69 -70.8 110.4 0.333 -80.7 -81.7 99.4 0.333 -96.7 -101.2 279.3 3.4 32 S 136.5 0.074 -172.8 0.333 -71.3 -73.3 110.4 0.333 -83 -84.1 94.8 0.333 -99.2 -103.7 321.3 2.1 33 S 139.6 0.079 -172.9 0.333 -73.4 -75.5 100.7 0.333 -85.2 -86.5 94.1 0.333 -101.6 -106.2 329 4.3 34 S 156.2 0.065 -173.7 0.333 -75.7 -77.9 115.1 0.333 -87.4 -88.8 106.9 0.333 -103 -107.8 263.5 2.7 35 S 133.1 0.075 -172.5 0.333 -77.9 -80.2 111.8 0.333 -89.5 -91 90.4 0.333 -105.3 -110 323 3.6 36 S 149.7 0.068 -173.3 0.333 -79.9 -82.4 102.3 0.333 -91.5 -93 92.8 0.333 -107.5 -112.2 329.4 1.9 37 S 154.7 0.064 -173 0.333 -82 -84.6 112.8 0.333 -93.5 -95.1 93.3 0.333 -109 -113.9 291.3 3.3 38
105
EXP 1 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t S 123.2 0.077 -172.5 0.333 -83.9 -86.7 101 0.333 -95.6 -97.1 94.1 0.333 -111.4 -116.1 350.6 3.4 39 S 150.4 0.065 -173.8 0.333 -85.9 -88.8 106.3 0.333 -97.5 -99.1 96.1 0.333 -113 -117.9 313.5 2.6 40 S 152.1 0.07 -173 0.333 -87.9 -90.9 112.8 0.333 -99.4 -101.1 94.2 0.333 -114.5 -119.5 304.5 2.9 41 S 113.8 0.096 -172.3 0.333 -90 -93 112.4 0.333 -101.7 -103.4 115.8 0.333 -117.1 -121.9 390.2 5.8 42
SW 195.2 0.077 -173.9 0.333 -92.3 -95.4 134.7 0.333 -104 -105.8 132.8 0.333 -118.8 -123.7 340.3 3.8 43 SW 164.1 0.075 -173.1 0.333 -94 -97.3 106.2 0.333 -105.5 -107.6 90.4 0.333 -120 -125.1 306.1 1.9 44 SW 132.4 0.094 -172.3 0.333 -95.6 -99.1 92.5 0.333 -107.4 -109.5 92.9 0.333 -122.4 -127.2 407.3 4.2 45 SW 194.4 0.081 -173.4 0.333 -97.4 -100.9 103 0.333 -109.2 -111.3 101.3 0.333 -123.9 -128.9 349.8 5.2 46 SW 163.5 0.068 -173.3 0.333 -99.2 -102.9 116.8 0.333 -110.6 -112.9 83.7 0.333 -124.6 -129.9 281.6 2.5 47 SW 130.5 0.082 -172.2 0.333 -100.8 -104.6 97 0.333 -112.3 -114.7 85.2 0.333 -126.9 -131.9 430 2.8 48 SW 151.2 0.093 -172.5 0.333 -102.3 -106.2 92.3 0.333 -113.8 -116.3 82.1 0.333 -128.5 -133.6 385.1 4.1 49 SW 179.3 0.068 -174.1 0.333 -103.9 -107.9 106 0.333 -115.2 -117.8 78.6 0.333 -128.8 -134.2 252.3 6.1 50 SW 126 0.075 -172.4 0.333 -105.4 -109.6 101.1 0.333 -116.6 -119.3 74.9 0.333 -130.8 -135.9 424.6 5.0 51 SW 133.9 0.099 -172.2 0.333 -107.3 -111.4 122.5 0.333 -118.9 -121.5 160.9 0.333 -132.5 -137.6 413.5 2.5 52 SW 171.5 0.068 -173.8 0.333 -108.9 -113.1 110.6 0.333 -120.2 -123 96.4 0.333 -133.1 -138.4 299.4 2.8 53 SW 119.4 0.072 -172.4 0.333 -110.5 -114.8 120.4 0.333 -121.4 -124.3 69.2 0.333 -134.4 -139.6 389.3 4.7 54 SW 126.1 0.09 -172.1 0.333 -111.9 -116.4 100.5 0.333 -123.2 -126.1 132.1 0.333 -136.2 -141.2 433 6.2 55 SW 148.8 0.072 -173.8 0.333 -113.3 -117.9 100.2 0.333 -124.3 -127.4 77.2 0.333 -136.9 -142.2 346.3 6.6 56 SW 137.1 0.07 -172.8 0.333 -114.8 -119.5 117.2 0.333 -125.6 -128.7 89.9 0.333 -138 -143.2 378.9 2.2 57 SW 140.5 0.076 -172.5 0.333 -116.3 -121 111.7 0.333 -127.4 -130.5 145 0.333 -139.8 -144.8 493.3 4.8 58 SW 129.2 0.079 -172.5 0.333 -118 -122.7 137.5 0.333 -131.1 -133.3 77.1 0.333 -155.5 -158 2862.3 3.6 59 SW 143.8 0.063 -173.5 0.333 -120.7 -124.5 119.3 0.333 -141.2 -143 1006.8 0.333 -166.9 -169.1 5483.9 3.5 60 SW 121.1 0.065 -172.5 -126.8 -158.8 -169.6 2.8 61 SW 134.7 0.073 -172.4 -130.2 -165.3 -169.5 2.6 62 SW 130.1 0.067 -173.6 -135.5 -166.5 -169.8 6.0 63 SW 144.2 0.062 -173.5 -140.6 -167.5 -170.8 5.3 64 SW 144.6 0.064 -173.4 -145.7 -168.5 -170.9 2.9 65 SW 141.5 0.064 -173.1 -152.3 -169.1 -170.9 1.9 66 SW 143.4 0.057 -173.3 -157 -169.6 -170.7 8.0 67 SW 152.9 0.056 -174.1 -164.6 -169.6 -170.9 8.3 68 SW 148.9 0.057 -173.6 -169 -170.1 -171.3 7.9 69 SW 155.1 0.053 -173.6 -169.8 -170.3 -171.3 3.6 70 SW 159.1 0.052 -174.2 -170 -170.5 -171.4 2.6 71 SW 161.9 0.051 -174.4 -170.2 -170.9 -171.8 7.4 72 SW 165.9 0.049 -174.4 -170.4 -171.3 -172.2 9.8 73 SW 163.7 0.049 -174.9 -170.7 -171.6 -172.5 4.0 74 SW 161.5 0.048 -175.2 -170.8 -171.9 -172.9 2.0 75 SW 158.1 0.048 -175.1 -171 -172.1 -173.2 1.2 76
106
EXP 1 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 157 0.046 -175.4 -171.2 -172.3 -173.4 6.7 77
I 161.4 0.044 -175.6 -171.2 -172.5 -173.6 12.4 78 I 160.4 0.044 -175.9 -171.3 -172.8 -173.8 4.0 79 I 167.6 0.042 -176 -171.5 -173 -174 3.4 80 I 179.5 0.04 -176.2 -171.6 -173.3 -174.4 2.0 81 I 194.7 0.037 -176.5 -171.9 -173.6 -174.7 8.8 82 I 215.5 0.035 -177.6 -172.3 -174 -175.2 12.4 83 I 230.7 0.035 -178.8 -173 -174.7 -175.8 4.0 84 I 236.6 0.035 -179.5 -174.3 -175.5 -176.7 2.3 85 I 242.8 0.034 -179.7 -175.2 -176.2 -177.4 10.3 86 I 243.9 0.033 -180 -175.9 -176.8 -177.9 12.4 87 I 241.7 0.032 -180.2 -176.2 -177.1 -178.2 12.4 88 I 239.3 0.031 -180.4 -176.5 -177.3 -178.5 2.7 89 I 239.7 0.03 -180.6 -176.7 -177.5 -178.7 3.4 90 I 238.1 0.029 -180.6 -176.9 -177.5 -178.8 2.5 91 I 236.7 0.028 -180.5 -177.1 -177.6 -178.8 6.5 92 I 235.2 0.027 -180.4 -177.3 -177.7 -178.9 12.4 93 I 233.6 0.026 -180.8 -177.6 -177.8 -179.1 10.7 94 I 229.6 0.025 -181 -177.8 -178 -179.3 4.7 95 I 226.9 0.024 -181.6 -178.2 -178.2 -179.6 3.3 96 I 223.6 0.024 -182.1 -178.6 -178.5 -179.8 2.3 97 I 222.6 0.023 -182.2 -178.8 -178.7 -180 12.4 98 I 221.6 0.022 -182.4 -178.9 -178.8 -180.1 12.4 99 I 221.2 0.021 -182.5 -179 -178.9 -180.3 3.1 100 I 220.6 0.021 -182.7 -179.2 -179 -180.4 4.7 101 I 219.2 0.02 -182.8 -179.2 -179.1 -180.6 2.9 102 I 218 0.019 -182.9 -179.3 -179.2 -180.7 8.4 103 I 217.1 0.019 -182.9 -179.4 -179.2 -180.7 10.4 104 I 214.6 0.018 -183 -179.4 -179.2 -180.8 6.1 105 I 213 0.017 -183.3 -179.7 -179.5 -181.1 7.9 106 I 212.2 0.017 -183.8 -180.1 -180 -181.5 9.6 107 I 211.4 0.016 -184 -180.3 -180.2 -181.9 10.0 108 I 210.8 0.016 -184.1 -180.5 -180.3 -182.1 10.4 109 I 209.4 0.015 -184.7 -180.9 -180.8 -182.6 12.4 110 I 209.1 0.014 -185 -181.2 -181.1 -182.9 9.3 111 I 207.4 0.014 -185.1 -181.3 -181.2 -183.1 9.7 112 I 204.3 0.014 -185.1 -181.4 -181.3 -183.2 6.8 113
107
EXP 2 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 69 1 8.6 0.333 21 22.4 1009.7 0.333 20.9 22.5 917.1 0.333 20 21.6 1330.2 0.0 1 N 45.5 1 4.5 0.333 20.8 21.5 272.3 0.333 20.8 21.7 186.3 0.333 20.1 20.8 225.5 0.0 2 N 11.8 1 1.9 0.333 20.3 20.8 287.1 0.333 20.2 21 257.4 0.333 19.5 20.1 360.7 0.0 3 N 17.8 1 5.9 0.333 20.2 20.6 114 0.333 20.2 20.8 45.2 0.333 19.5 19.9 141.8 0.0 4 N 38.1 1 8.5 0.333 20.1 20.4 95.1 0.333 20 20.6 25.3 0.333 19.3 19.7 128.1 0.0 5 N 48.1 1 6.3 0.333 19.5 20 206.5 0.333 19.5 20.2 131.5 0.333 18.8 19.3 218.3 0.0 6 N 53 1 3.3 0.333 18.8 19.3 265.6 0.333 18.9 19.6 183.2 0.333 18.2 18.7 265.4 0.0 7 N 55.5 1 0.5 0.333 18 18.5 278.6 0.333 18.1 18.9 201.9 0.333 17.4 18 269.8 0.0 8 N 56.2 1 -2.5 0.333 17.1 17.6 297.4 0.333 17.3 18 206.1 0.333 16.6 17.2 287.7 0.0 9 N 54 1 -5.2 0.333 16.2 16.6 264.6 0.333 16.3 17.1 196.6 0.333 15.6 16.2 259.4 0.0 10 N 49 1 -10.6 0.333 15.2 15.6 146.2 0.333 15.4 16.2 108.7 0.333 14.7 15.2 144.5 0.0 11 N 56.4 1 -36.8 0.333 13.6 14.1 161.6 0.333 13.8 14.8 120.2 0.333 12.4 13.2 237.2 0.0 12 N 57.6 1 -53.3 0.333 11.8 12.3 177.2 0.333 11.8 12.9 134.4 0.333 9.2 10.2 306.1 0.0 13 N 57.7 1 -63.5 0.333 9.9 10.3 169 0.333 9.7 10.9 130.4 0.333 6.3 7.1 278.7 0.0 14 N 60.7 1 -74.5 0.333 7.9 8.3 169.1 0.333 7.3 8.6 138.8 0.333 2.8 3.4 329.3 0.0 15 N 60.4 1 -78.9 0.333 5.8 6.1 163.7 0.333 4.8 6.1 136 0.333 -0.8 -0.3 331.3 0.0 16 N 58.6 1 -86.4 0.333 3.5 3.9 171.8 0.333 2 3.3 149.1 0.333 -4.3 -4.2 337.6 0.0 17 N 57.2 1 -90.3 0.333 1.4 1.6 163.6 0.333 -0.6 0.6 142 0.333 -7.6 -7.8 326.4 1.2 18 N 56.1 0.558 -93.1 0.333 -0.6 -0.5 143.4 0.333 -3.1 -2 125.8 0.333 -10.9 -11.3 313.2 1.8 19 N 59.7 0.335 -100.7 0.333 -2.7 -2.5 116.6 0.333 -5.8 -4.7 108.9 0.333 -14.5 -15.1 281.7 1.5 20 N 60.7 0.242 -122.3 0.333 -4.7 -4.6 86.1 0.333 -8.6 -7.5 87 0.333 -18.2 -19 216.3 2.2 21 N 56.5 0.2 -164.7 0.333 -6.8 -6.7 84.2 0.333 -11.3 -10.3 80.6 0.333 -21.4 -22.5 199.5 1.6 22 N 55.5 0.167 -168.5 0.333 -8.8 -8.7 81.3 0.333 -13.7 -12.9 74.4 0.333 -24.3 -25.7 189.1 1.7 23 N 51.9 0.15 -168 0.333 -10.7 -10.7 76.3 0.333 -16.1 -15.3 71.2 0.333 -27.2 -28.8 190.3 2.2 24 N 56.5 0.122 -169.4 0.333 -12.6 -12.6 76.2 0.333 -18.3 -17.6 64.8 0.333 -29.6 -31.5 176.9 1.8 25 N 58.4 0.106 -169.4 0.333 -14.5 -14.6 74.9 0.333 -20.7 -20 68.8 0.333 -32.7 -34.6 204.8 2.1 26 N 58.5 0.095 -168.9 0.333 -16.5 -16.6 77.3 0.333 -23 -22.4 68.2 0.333 -35.4 -37.5 200.8 1.4 27 N 62.5 0.083 -168.5 0.333 -18.6 -18.7 83.5 0.333 -25.5 -24.9 76.2 0.333 -38.2 -40.4 203.8 2.1 28 N 63.2 0.075 -168.8 0.333 -20.8 -20.9 85.6 0.333 -28 -27.5 77.9 0.333 -41 -43.3 212.6 2.0 29 N 59.2 0.073 -168.9 0.333 -22.9 -23.1 86 0.333 -30.4 -30 74.9 0.333 -43.8 -46.3 216.1 2.1 30 N 52.3 0.074 -169.6 0.333 -25.1 -25.3 86.5 0.333 -32.6 -32.3 72 0.333 -45.6 -48.4 171.5 2.2 31 N 50.4 0.07 -170 0.333 -27.2 -27.5 85.8 0.333 -34.8 -34.6 70.6 0.333 -47.3 -50.2 161.4 2.5 32 N 53.4 0.063 -170.4 0.333 -31.2 -29.6 81.6 0.333 -39 -36.8 70 0.333 -51.4 -52.1 165.5 2.0 33 N 54.3 0.059 -170.7 0.333 -33.1 -31.7 81.5 0.333 -41 -38.9 68.8 0.333 -53.8 -54.2 181.2 2.9 34 N 55.8 0.054 -170.9 0.333 -35 -33.8 79.9 0.333 -43 -41 64.6 0.333 -56 -56.6 199.5 1.7 35 N 57.1 0.051 -170.9 0.333 -36.9 -35.8 81 0.333 -45.1 -43.1 65.3 0.333 -58.3 -58.9 197.9 2.1 36 N 58.9 0.047 -170.8 0.333 -38.8 -37.8 79.6 0.333 -47.1 -45.1 64.3 0.333 -61 -61.3 207.4 2.5 37
SW 60.6 0.044 -171 0.333 -40.7 -39.8 79 0.333 -49.1 -47.2 60 0.333 -63.4 -64 229.9 2.5 38
108
EXP 2 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 59.9 0.043 -171.1 0.333 -42.6 -41.8 82.5 0.333 -51.2 -49.2 56.7 0.333 -65.7 -66.6 229.7 2.5 39 SW 63.8 0.039 -171.2 0.333 -44.5 -43.7 79.3 0.333 -53.2 -51.3 63.9 0.333 -68.4 -69.1 226.2 2.3 40 SW 72.4 0.035 -170.8 0.333 -46.3 -45.7 81.9 0.333 -55.4 -53.4 57.9 0.333 -71.1 -71.8 257.9 2.3 41 SW 74.5 0.033 -170.6 0.333 -48.1 -47.6 78.5 0.333 -57.5 -55.6 60.3 0.333 -73.6 -74.7 267.4 3.2 42 SW 75 0.032 -170.5 0.333 -50 -49.5 82.5 0.333 -59.7 -57.8 63.3 0.333 -76.1 -77.3 268.4 2.7 43 SW 74 0.031 -170.2 0.333 -52 -51.5 82.9 0.333 -61.9 -60 66.5 0.333 -78.7 -80 274.9 3.5 44 SW 82.6 0.028 -169.8 0.333 -53.9 -53.4 85.9 0.333 -64.2 -62.2 66.8 0.333 -81 -82.7 292.9 5.6 45 SW 84.4 0.027 -169.5 0.333 -55.9 -55.4 87 0.333 -66.4 -64.6 75.4 0.333 -83.5 -85.2 281.8 4.6 46 SW 78.6 0.028 -169.5 0.333 -57.9 -57.5 89.5 0.333 -68.6 -66.9 74.8 0.333 -85.7 -87.7 293.1 4.0 47 SW 83.3 0.026 -169.6 0.333 -59.8 -59.5 89.8 0.333 -70.7 -69.1 71.9 0.333 -87.8 -90.1 291.2 4.0 48 SW 79.7 0.026 -169.5 0.333 -61.8 -61.6 90.4 0.333 -72.9 -71.3 72 0.333 -90 -92.3 285.7 3.5 49 SW 88.7 0.024 -169.6 0.333 -63.7 -63.6 90.9 0.333 -74.9 -73.5 76.3 0.333 -91.9 -94.5 292.5 3.3 50 SW 86.4 0.024 -169.7 0.333 -65.6 -65.6 90.3 0.333 -76.8 -75.6 71.7 0.333 -93.8 -96.5 282.5 2.8 51 SW 79.2 0.024 -169.9 0.333 -67.5 -67.6 88.1 0.333 -78.7 -77.6 67.2 0.333 -95.6 -98.5 284.8 4.2 52 SW 83.3 0.023 -169.9 0.333 -69.3 -69.5 88.3 0.333 -80.6 -79.6 66.9 0.333 -97.6 -100.4 286.2 3.7 53 SW 83.9 0.022 -169.8 0.333 -71.1 -71.5 87.5 0.333 -82.4 -81.5 63 0.333 -99.3 -102.3 299.4 3.3 54 SW 85.7 0.022 -170 0.333 -72.9 -73.4 88 0.333 -84.2 -83.4 64 0.333 -101 -104.1 290.7 4.7 55 SW 94.8 0.02 -169.8 0.333 -74.6 -75.2 87.2 0.333 -85.9 -85.3 65.6 0.333 -102.7 -105.9 294 4.0 56 SW 78.9 0.022 -169.9 0.333 -76.3 -77 83.7 0.333 -87.7 -87 58.9 0.333 -104.2 -107.6 297.6 6.2 57 SW 76.8 0.022 -170.2 0.333 -78 -78.9 88.8 0.333 -89.3 -88.8 63.4 0.333 -105.8 -109.2 285.9 4.2 58 SW 88.3 0.02 -170 0.333 -79.8 -80.7 87.4 0.333 -91.1 -90.6 59.1 0.333 -107.3 -110.8 300 3.9 59 SW 93.7 0.019 -169.8 0.333 -81.4 -82.5 91.9 0.333 -92.6 -92.3 67.3 0.333 -108.7 -112.3 300 3.9 60 SW 81.8 0.02 -169.5 0.333 -83.1 -84.2 86.7 0.333 -94.3 -94 57.4 0.333 -110.1 -113.8 292.2 4.3 61 SW 80.7 0.02 -169.5 0.333 -84.7 -86 91.1 0.333 -95.9 -95.6 63.8 0.333 -111.5 -115.2 297.2 4.4 62 SW 80.7 0.02 -169.3 0.333 -86.5 -87.8 92.9 0.333 -97.6 -97.3 68.3 0.333 -112.8 -116.6 305.1 4.2 63 SW 81.7 0.019 -169.1 0.333 -88.2 -89.6 98.9 0.333 -99.2 -99 75.2 0.333 -114.1 -117.9 294.3 4.3 64 SW 82 0.019 -169.1 0.333 -89.9 -91.4 102.6 0.333 -100.8 -100.7 73 0.333 -115.4 -119.1 294.7 5.1 65 SW 82.8 0.018 -169.1 0.333 -91.4 -93.2 99.8 0.333 -102.3 -102.3 74.4 0.333 -116.8 -120.4 305 5.2 66 SW 82.6 0.018 -169.2 0.333 -93 -94.9 96.3 0.333 -103.8 -103.9 68.3 0.333 -117.9 -121.8 310.9 5.5 67 SW 81.2 0.018 -169.6 0.333 -94.5 -96.5 96.5 0.333 -105.2 -105.5 74.1 0.333 -119.2 -123 294.7 5.3 68 SW 85.7 0.017 -169.8 0.333 -95.9 -98.1 91.4 0.333 -106.6 -106.9 64.6 0.333 -120.5 -124.2 304.5 4.7 69 SW 83.8 0.017 -169.7 0.333 -97.3 -99.7 90.5 0.333 -107.8 -108.4 64.7 0.333 -121.8 -125.5 313.5 6.3 70 SW 80.4 0.017 -170.1 0.333 -98.6 -101.1 86 0.333 -109.1 -109.7 52.7 0.333 -123 -126.8 330.5 5.7 71 SW 81 0.017 -170.2 0.333 -99.9 -102.5 86.4 0.333 -110.3 -111 56.4 0.333 -124.3 -128 318.5 8.6 72 SW 90.3 0.016 -170 0.333 -101.2 -104 87 0.333 -111.6 -112.3 46.2 0.333 -125.4 -129.4 341.2 5.9 73 SW 84.4 0.016 -170.3 0.333 -102.4 -105.3 83.7 0.333 -112.9 -113.6 58.4 0.333 -126.6 -130.5 328.1 5.6 74 SW 87.5 0.016 -170.3 0.333 -103.6 -106.6 82.2 0.333 -114.1 -114.9 58.7 0.333 -127.7 -131.7 336.1 5.9 75 SW 89.9 0.016 -170.2 0.333 -104.8 -107.9 84.7 0.333 -115.2 -116.1 48.1 0.333 -128.7 -132.9 344.3 6.0 76
109
EXP 2 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 79.3 0.017 -170.9 0.333 -105.9 -109.2 77.3 0.333 -116.3 -117.3 46.8 0.333 -129.7 -133.9 324.5 6.2 77 SW 84.8 0.016 -171.2 0.333 -107 -110.4 77.8 0.333 -117.3 -118.4 40.7 0.333 -130.7 -134.9 326.2 5.7 78 SW 83.8 0.016 -171.4 0.333 -108.1 -111.5 73.6 0.333 -118.4 -119.5 41.6 0.333 -131.7 -135.9 332.6 7.2 79 SW 82.8 0.016 -171.5 0.333 -109.1 -112.7 77.6 0.333 -119.4 -120.6 41.9 0.333 -132.7 -136.9 345.3 6.1 80 SW 83.1 0.016 -171.7 0.333 -110.1 -113.8 70.7 0.333 -120.5 -121.7 37.7 0.333 -133.7 -138 351.6 5.1 81 SW 85.4 0.015 -171.9 0.333 -111.1 -114.9 72.8 0.333 -121.5 -122.7 40.7 0.333 -134.6 -139 352.1 6.3 82 SW 83.2 0.016 -172 0.333 -112.1 -115.9 64.7 0.333 -122.5 -123.8 38.1 0.333 -135.6 -139.9 356.4 6.0 83 SW 103.7 0.014 -171.9 0.333 -113.2 -117 75.8 0.333 -123.8 -124.8 45.9 0.333 -136.3 -140.9 366.1 6.4 84 SW 90.4 0.015 -171.5 0.333 -114.3 -118 69.7 0.333 -125.9 -126.1 84.5 0.333 -144.8 -141.6 328.7 5.1 85 SW 72.7 0.017 -172.1 0.333 -116 -119.2 84.3 0.333 -133.2 -127.6 23.9 0.333 -162.5 -148.6 1487.5 6.5 86 SW 77.8 0.016 -172.3 0.333 -118.4 -120.4 76.4 0.333 -141.4 -133.3 435.5 0.333 -162.8 -164.5 4170.2 6.5 87 SW 77.1 0.016 -172.3 0.333 -121 -121.7 50.2 0.333 -147 -142 1144.7 0.333 -162.1 -167.1 4361.8 6.7 88 SW 87.4 0.014 -172.1 -123.4 -148.7 -167.6 6.4 89 SW 85.6 0.015 -172.2 -125.6 -152.6 -167.7 6.6 90 SW 85.3 0.015 -172.1 -128.3 -154.9 -167.9 5.5 91 SW 86.3 0.015 -172.1 -131.1 -157.6 -168 6.8 92 SW 84.4 0.015 -172.5 -134 -159.6 -168.1 6.4 93 SW 82.2 0.015 -172.6 -136.9 -161.7 -168.4 5.8 94 SW 82.7 0.015 -172.6 -139.5 -162.3 -168.6 5.8 95 SW 87.7 0.014 -172.7 -142 -163.7 -168.8 4.7 96 SW 85.5 0.015 -172.7 -144.4 -164.4 -168.9 8.2 97 SW 82 0.015 -172.8 -146.5 -164.4 -168.9 8.4 98 SW 85 0.015 -172.7 -148.5 -165 -169 6.0 99 SW 87.3 0.014 -172.8 -150.3 -165.9 -169 6.9 100 SW 86.1 0.014 -172.9 -151.9 -166.3 -169.1 5.6 101 SW 90.5 0.014 -173 -153.4 -166.9 -169.2 6.6 102 SW 91.8 0.014 -173.1 -155 -167.4 -169.3 6.3 103 SW 88 0.014 -173.1 -157 -167.8 -169.4 8.5 104 SW 92.2 0.014 -173.3 -158.4 -168.2 -169.5 5.3 105 SW 75.8 0.016 -173.9 -159.3 -168.1 -169.7 5.7 106 SW 88.4 0.014 -174 -161.1 -169.1 -170.2 8.3 107 SW 87.6 0.014 -173.9 -163.3 -169.5 -170.4 5.9 108 SW 92.4 0.014 -173.9 -164.6 -169.8 -170.4 4.9 109 SW 85.9 0.014 -174.2 -166.6 -170 -170.5 10.1 110 SW 86.5 0.014 -174.4 -167.2 -170.2 -170.6 7.8 111 SW 84.1 0.014 -174.6 -167.1 -170.3 -170.7 6.3 112 SW 83.9 0.01 -174.5 -166.9 -170.3 -170.9 7.2 113 SW 93.9 0.01 -174.5 -166.7 -170.4 -171 8.6 114
110
EXP 2 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 80 0.01 -174.8 -166.5 -170.3 -171.1 5.6 115 SW 93.3 0.01 -174.7 -167.4 -170.7 -171.2 6.0 116 SW 94.3 0.01 -174.6 -167.4 -170.6 -171.3 7.4 117 SW 85 0.01 -174.7 -167.2 -170.5 -171.3 5.5 118 SW 79.5 0.01 -175 -166.9 -170.5 -171.3 6.8 119 SW 86.2 0.01 -174.9 -166.9 -170.7 -171.4 7.0 120 SW 90 0.01 -174.8 -167.9 -170.9 -171.5 6.3 121 SW 83.7 0.01 -174.9 -167.7 -170.7 -171.5 7.5 122 SW 78.8 0.01 -175.1 -167.4 -170.6 -171.6 9.2 123 SW 83.5 0.01 -175.2 -167.2 -170.9 -171.7 6.7 124 SW 86.1 0.01 -175.2 -167.1 -171 -171.8 6.5 125 SW 86.1 0.01 -175.2 -167.2 -171.1 -171.9 6.2 126 SW 92 0.01 -175.1 -167.6 -171.1 -172 6.6 127 SW 98.1 0.02 -175.2 -168.5 -171.4 -172 6.6 128 SW 87.6 0.02 -175.3 -169.8 -171.6 -172.1 6.8 129 SW 91.5 0.01 -175.3 -170 -171.6 -172.1 7.1 130 SW 78 0.02 -175.7 -169.7 -171.7 -172.2 6.9 131 SW 80.2 0.01 -175.8 -169.5 -171.7 -172.3 7.0 132 SW 88.5 0.01 -175.8 -170.5 -171.9 -172.5 6.3 133 SW 87.3 0.01 -175.7 -171.2 -172.1 -172.6 5.8 134 SW 85.2 0.02 -175.7 -171.1 -172.2 -172.6 10.7 135 SW 80.6 0.02 -175.9 -170.6 -172.1 -172.7 6.7 136 SW 80.2 0.01 -176.1 -170.1 -172.2 -172.7 6.5 137 SW 86.4 0.01 -175.9 -170.7 -172.2 -172.9 6.9 138 SW 90.7 0.02 -175.9 -170.7 -172.3 -172.9 7.5 139 SW 95.5 0.02 -175.8 -170.5 -172.3 -172.9 7.0 140 SW 87.4 0.02 -176 -170.2 -172.2 -173 7.5 141 SW 81.6 0.02 -176.2 -170 -172.2 -173 8.4 142 SW 87.8 0.02 -176.1 -169.8 -172.2 -173.1 9.2 143 SW 87.5 0.02 -176.2 -169.7 -172.3 -173.1 7.7 144 SW 83.8 0.02 -176.2 -169.5 -172.2 -173.1 9.4 145 SW 92 0.02 -176.2 -169.4 -172.3 -173.2 7.9 146 SW 89.6 0.02 -176.3 -169.9 -172.5 -173.2 8.2 147 SW 87.5 0.02 -176.4 -169.7 -172.5 -173.2 7.9 148
111
EXP 3 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 32.8 1 8.4 0.333 22.3 23.3 745.4 0.333 22.4 23.6 556.6 0.333 21.5 22.8 1018.8 0.0 1 N 33.2 1 7.4 0.333 22.3 22.9 134.3 0.333 22.5 23.2 65.9 0.333 21.8 22.3 101 0.0 2 N 33.2 1 6.2 0.333 21.9 22.4 189.3 0.333 22 22.7 116.9 0.333 21.4 21.9 201.7 0.0 3 N 33.5 1 5 0.333 21.3 21.9 212.9 0.333 21.5 22.3 124 0.333 20.9 21.4 202.1 0.0 4 N 33.5 1 3.8 0.333 20.8 21.4 199 0.333 21.1 21.8 117 0.333 20.4 21 197.2 0.0 5 N 33.6 1 2.1 0.333 20.3 20.8 201.8 0.333 20.5 21.3 126.8 0.333 19.9 20.4 193.9 0.0 6 N 33.9 1 0.1 0.333 19.7 20.2 192.6 0.333 20 20.7 112.6 0.333 19.3 19.9 187.7 0.0 7 N 34.2 1 -3.5 0.333 18.9 19.4 196 0.333 19.2 20 129.2 0.333 18.6 19.2 185.2 0.0 8 N 34.1 1 -10.2 0.333 17.7 18.2 261.6 0.333 18.1 18.9 188.2 0.333 17.4 18 258.8 0.0 9 N 34.3 1 -14.6 0.333 16.9 17.3 171 0.333 17.3 18.1 113.7 0.333 16.5 17.1 187.5 0.0 10 N 34.7 1 -21.9 0.333 15.6 16 183.1 0.333 16 16.9 132.6 0.333 14.9 15.6 213.7 0.0 11 N 36.3 1 -34.8 0.333 14.7 15 118 0.333 14.9 15.8 81 0.333 13.2 13.9 210.7 0.0 12 N 38.7 1 -48 0.333 13.6 13.9 116.6 0.333 13.6 14.6 81.6 0.333 10.9 11.5 256.1 0.0 13 N 40.8 0.455 -57.6 0.333 12.5 12.7 109.1 0.333 12.2 13.1 78.3 0.333 8.3 8.8 277.7 0.0 14 S 40.2 0.407 -65.6 0.333 11.3 11.6 101.2 0.333 10.5 11.6 82.3 0.333 5.5 5.8 294.6 1.2 15 S 42.8 0.34 -71.1 0.333 10.1 10.4 93.4 0.333 8.7 9.8 82 0.333 2.5 2.6 301.4 1.0 16 S 42.4 0.311 -80.3 0.333 8.7 9 105.9 0.333 6.6 7.8 95.2 0.333 -0.9 -1 340.3 1.3 17 S 41.5 0.287 -84.1 0.333 7.3 7.7 98.4 0.333 4.6 5.7 95.1 0.333 -3.8 -4.2 320.6 1.2 18 S 41.9 0.26 -84.4 0.333 6 6.3 97.6 0.333 2.6 3.6 96.9 0.333 -6.2 -6.9 292.5 1.1 19 S 42.6 0.235 -85.5 0.333 4.5 4.9 103.5 0.333 0.6 1.6 98.8 0.333 -8.6 -9.6 302.3 0.9 20 S 40.4 0.228 -86.2 0.333 2.8 3.3 110 0.333 -1.4 -0.4 95.7 0.333 -10.8 -12 281.6 1.2 21 S 45.9 0.188 -87.6 0.333 1.3 1.7 104.7 0.333 -3.3 -2.5 96.7 0.333 -13.2 -14.4 297 1.3 22 S 42.1 0.192 -89.1 0.333 -0.3 0.1 109.1 0.333 -5.2 -4.4 94.8 0.333 -15.2 -16.6 283 1.0 23 S 44.5 0.169 -88.8 0.333 -1.8 -1.5 98.5 0.333 -7 -6.3 85.2 0.333 -17.3 -18.8 271.5 1.3 24 S 42.8 0.166 -94.6 0.333 -3.5 -3.1 102.9 0.333 -8.9 -8.2 86.6 0.333 -19.4 -21 271.9 1.1 25 S 41.5 0.16 -98.4 0.333 -5.1 -4.8 108.5 0.333 -10.8 -10.1 95.5 0.333 -21.8 -23.5 335.3 1.1 26 S 46.8 0.135 -90.9 0.333 -6.8 -6.5 105.1 0.333 -12.5 -11.9 77.3 0.333 -23.2 -25.1 222 1.1 27 S 39 0.153 -101.3 0.333 -8.5 -8.3 117.2 0.333 -14.6 -13.9 106.6 0.333 -25.6 -27.4 324.9 1.1 28 S 46.2 0.122 -94 0.333 -10.2 -10.1 119.3 0.333 -16.4 -15.9 96.3 0.333 -27.2 -29.2 279.7 1.2 29 S 46.3 0.117 -95.2 0.333 -12.1 -12 86.8 0.333 -18.1 -17.6 60.6 0.333 -28.5 -30.7 149.9 2.4 30 S 39.4 0.129 -137.5 0.333 -13.9 -13.8 67.5 0.333 -20.2 -19.7 60 0.333 -31.2 -33.1 170.2 3.3 31 S 50.6 0.097 -168.5 0.333 -15.6 -15.7 65.6 0.333 -21.9 -21.6 51.3 0.333 -32.6 -34.8 126.8 3.3 32 S 51.9 0.093 -171 0.333 -17.4 -17.5 66.9 0.333 -23.7 -23.4 50.3 0.333 -34.2 -36.5 128.2 3.4 33 S 41.7 0.109 -172.1 0.333 -19 -19.3 62.2 0.333 -25.7 -25.4 55.2 0.333 -37.5 -39.5 205 1.7 34 S 59.7 0.074 -172 0.333 -20.6 -20.9 59.5 0.333 -27.5 -27.2 45.7 0.333 -39.6 -41.9 170.2 4.1 35 S 50.7 0.086 -172.4 0.333 -22.3 -22.7 61.9 0.333 -29.1 -29 45.7 0.333 -40.8 -43.5 129.5 2.0 36 S 49.3 0.082 -172 0.333 -23.8 -24.3 57.9 0.333 -31.1 -30.8 43 0.333 -44.3 -46.6 226.4 4.5 37 S 45.8 0.085 -172 0.333 -25.4 -26 61 0.333 -32.9 -32.7 44.4 0.333 -46.5 -49.2 192.6 3.2 38
112
EXP 3 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t S 57.4 0.066 -172.5 0.333 -27.1 -27.7 62.7 0.333 -34.5 -34.5 41.8 0.333 -47.1 -50.3 115.5 1.5 39 S 52.1 0.072 -172.3 0.333 -28.8 -29.4 63.8 0.333 -36.5 -36.3 49 0.333 -49.9 -52.8 203.5 3.5 40 S 41.7 0.083 -172.2 0.333 -30.3 -31.1 60.9 0.333 -38.3 -38.2 40.8 0.333 -52.9 -55.8 232.6 2.5 41 S 58.8 0.057 -172.4 0.333 -31.9 -32.7 59.7 0.333 -39.9 -40 43.9 0.333 -53.6 -57.1 132 1.4 42 S 61 0.056 -172.7 0.333 -33.7 -34.5 68.2 0.333 -41.8 -41.9 48.6 0.333 -55.3 -58.7 165.5 3.7 43 S 48.1 0.068 -172.2 0.333 -35.3 -36.2 63.3 0.333 -43.7 -43.7 42.9 0.333 -58.6 -61.7 251.9 1.9 44 S 54.3 0.057 -172.5 0.333 -36.9 -37.9 61.9 0.333 -45.5 -45.6 41.2 0.333 -60.5 -64 203.2 3.3 45 S 66.4 0.047 -172.7 0.333 -38.6 -39.7 68.8 0.333 -47 -47.3 43.6 0.333 -60.8 -64.8 114.3 3.4 46 S 55.2 0.056 -172.3 0.333 -40.3 -41.4 66.2 0.333 -49 -49.2 45.3 0.333 -63.7 -67.1 228.1 2.2 47 S 42 0.067 -172.6 0.333 -41.8 -43.1 61.6 0.333 -50.7 -51 42.2 0.333 -66 -69.6 231.5 4.5 48 S 63.4 0.043 -172.3 0.333 -43.5 -44.7 64.6 0.333 -52.3 -52.7 41.8 0.333 -66.6 -70.6 137 4.8 49 S 65 0.044 -172.8 0.333 -45.2 -46.5 72 0.333 -54 -54.4 49.4 0.333 -68 -71.9 163 3.5 50 S 51.1 0.053 -172 0.333 -46.7 -48.2 62.5 0.333 -55.9 -56.2 42.6 0.333 -71.1 -74.6 266 1.6 51 S 45.4 0.055 -172.3 0.333 -48.4 -49.9 66.6 0.333 -57.6 -58 43.5 0.333 -72.8 -76.7 210.3 3.8 52 S 61.9 0.04 -173 0.333 -50 -51.6 68.9 0.333 -59 -59.6 44.5 0.333 -72.7 -77 100.2 3.5 53 S 59.4 0.042 -172.6 0.333 -51.7 -53.3 70.1 0.333 -60.8 -61.3 50.1 0.333 -74.7 -78.6 197 3.9 54 S 49.5 0.048 -172.3 0.333 -53.2 -54.9 63.5 0.333 -62.4 -63 41.4 0.333 -77.4 -81.1 259.1 5.4 55 S 44.4 0.05 -172.7 0.333 -54.8 -56.6 68.9 0.333 -64.1 -64.8 47.3 0.333 -78.8 -82.8 198.8 4.4 56 S 67 0.033 -173.1 0.333 -56.4 -58.3 70.8 0.333 -65.5 -66.3 47.2 0.333 -78.9 -83.2 111.8 2.9 57 S 59 0.039 -172.6 0.333 -58.1 -60 72.2 0.333 -67.2 -67.9 46.8 0.333 -80.8 -84.8 204.6 6.1 58 S 51 0.042 -172.6 0.333 -59.5 -61.6 63.1 0.333 -68.7 -69.5 38.8 0.333 -83.3 -87.1 256.4 5.1 59 S 50.1 0.041 -172.9 0.333 -61 -63.2 69.4 0.333 -70.3 -71.1 41.5 0.333 -84.8 -89 216.3 3.3 60 S 61.9 0.033 -173.3 0.333 -62.6 -64.8 68.8 0.333 -71.7 -72.7 49 0.333 -85.2 -89.6 137.1 2.3 61 S 66.5 0.031 -172.7 0.333 -64 -66.4 68 0.333 -73.3 -74.3 45.9 0.333 -87.2 -91.3 225.7 4.3 62 S 55.4 0.036 -172.4 0.333 -65.5 -67.9 68.2 0.333 -74.9 -75.8 39.3 0.333 -89.6 -93.6 268.7 3.8 63 S 46.1 0.041 -173 0.333 -66.9 -69.4 64.4 0.333 -76.4 -77.4 35.6 0.333 -91.3 -95.6 243.7 2.1 64 S 66.4 0.028 -173.5 0.333 -68.4 -70.9 70 0.333 -77.8 -78.9 43.1 0.333 -91.7 -96.4 156.4 6.9 65 S 68.1 0.029 -173.1 0.333 -69.9 -72.5 69.4 0.333 -79.3 -80.4 47.2 0.333 -93 -97.5 192.9 4.6 66 S 61 0.031 -172.4 0.333 -71.2 -73.9 65.7 0.333 -80.8 -81.9 33.6 0.333 -95.6 -99.8 295.9 3.1 67 S 50.3 0.035 -172.6 0.333 -72.6 -75.4 65.4 0.333 -82.2 -83.4 35.5 0.333 -97.4 -101.8 266.6 3.7 68 S 50 0.033 -173.2 0.333 -74 -76.8 67.6 0.333 -83.6 -84.8 36 0.333 -98.3 -103 203.8 3.9 69 S 61.8 0.027 -173.5 0.333 -75.4 -78.3 71 0.333 -84.8 -86.2 45 0.333 -98 -103 106.9 3.4 70 S 58.4 0.029 -172.6 0.333 -76.8 -79.8 69.4 0.333 -86.4 -87.7 48.1 0.333 -99.8 -104.3 230.1 3.6 71 S 47.9 0.033 -172.5 0.333 -78.2 -81.2 70.6 0.333 -87.7 -89 36 0.333 -101.7 -106.1 266.3 3.5 72 S 41.5 0.036 -172.9 0.333 -79.6 -82.8 75.1 0.333 -89 -90.5 49.2 0.333 -101.9 -107 147.2 3.8 73 S 59.7 0.025 -173.2 0.333 -81 -84.3 74.9 0.333 -90.2 -91.7 45.7 0.333 -102.2 -106.6 136.8 2.9 74 S 63.3 0.024 -172.8 0.333 -82.5 -85.8 78.2 0.333 -91.5 -93 53.9 0.333 -102.9 -107.4 150.3 2.5 75 S 56.3 0.027 -172.5 0.333 -83.7 -87.1 69.7 0.333 -92.7 -94.2 31.9 0.333 -105.4 -109.5 296.5 4.6 76
113
EXP 3 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t S 48 0.03 -173.1 0.333 -85 -88.5 69.1 0.333 -93.9 -95.5 38.9 0.333 -106.7 -111 237.6 5.4 77 S 63.2 0.022 -173.5 0.333 -86.2 -89.8 72.7 0.333 -95.1 -96.8 42.6 0.333 -107.2 -111.8 170.7 3.6 78 S 67.7 0.021 -173.1 0.333 -87.5 -91.2 73.8 0.333 -96.3 -98 41.9 0.333 -108 -112.6 186.7 4.4 79 S 60.6 0.023 -172.6 0.333 -88.7 -92.5 68.4 0.333 -97.6 -99.3 41.7 0.333 -110 -114.3 278.8 4.5 80 S 51.1 0.026 -173.1 0.333 -89.9 -93.7 67.7 0.333 -98.8 -100.5 32.8 0.333 -111.4 -115.9 257.8 4.8 81 S 64.4 0.02 -173.7 0.333 -91 -94.9 66.8 0.333 -99.9 -101.7 37.4 0.333 -112.2 -116.9 210.4 5.3 82 S 71.4 0.019 -173.5 0.333 -92.2 -96.2 72.1 0.333 -101.1 -102.9 42.5 0.333 -112.9 -117.6 189.5 5.4 83 S 68.4 0.02 -172.6 0.333 -93.3 -97.4 68 0.333 -102.2 -104 31.6 0.333 -114.8 -119.3 295.8 5.3 84 S 56.6 0.023 -172.7 0.333 -94.3 -98.5 63.1 0.333 -103.4 -105.2 33.2 0.333 -116.3 -120.9 287.5 4.8 85 S 51.1 0.024 -173.3 0.333 -95.4 -99.6 63.9 0.333 -104.5 -106.4 32.4 0.333 -117.3 -122.1 243.8 5.3 86 S 63.5 0.019 -174 0.333 -96.6 -100.8 72.8 0.333 -105.6 -107.6 38.6 0.333 -117.6 -122.6 178.9 5.8 87 S 74.7 0.017 -173.6 0.333 -97.7 -102 71.9 0.333 -106.8 -108.7 44.2 0.333 -118.6 -123.4 227 4.7 88 S 68.7 0.018 -172.8 0.333 -98.7 -103.1 65.3 0.333 -107.8 -109.8 26.9 0.333 -120.4 -125 315.6 5.2 89 S 59.5 0.02 -172.9 0.333 -99.7 -104.1 60.3 0.333 -108.9 -110.9 30.4 0.333 -121.8 -126.6 308.1 4.8 90 S 56.6 0.02 -173.5 0.333 -100.7 -105.2 62.9 0.333 -110 -112 29.5 0.333 -122.8 -127.8 272.8 5.4 91 S 72.1 0.016 -174 0.333 -101.8 -106.3 71.3 0.333 -111.1 -113.1 31.1 0.333 -123.6 -128.7 246.7 9.7 92 S 75.7 0.016 -173.5 0.333 -102.8 -107.4 66.5 0.333 -112.1 -114.2 24.9 0.333 -124.9 -129.9 304.8 6.3 93 S 72.9 0.016 -173.2 0.333 -103.7 -108.4 60.5 0.333 -113.2 -115.3 26.6 0.333 -126.4 -131.3 332.8 6.5 94 S 72.8 0.016 -173.2 0.333 -104.6 -109.3 56.8 0.333 -114.3 -116.4 27.6 0.333 -127.9 -132.9 366.4 7.0 95 S 69.6 0.016 -173.3 0.333 -105.6 -110.3 63 0.333 -115.4 -117.5 26.1 0.333 -129.4 -134.5 368.2 4.4 96 S 73.5 0.015 -173.6 0.333 -106.6 -111.3 60.9 0.333 -116.4 -118.6 24.6 0.333 -130.2 -135.5 312.5 4.5 97 S 83.9 0.013 -173.5 0.333 -107.6 -112.3 67.7 0.333 -117.5 -119.7 25.5 0.333 -131.3 -136.6 334.7 5.7 98 S 83.1 0.014 -173.2 0.333 -108.5 -113.3 60.7 0.333 -118.5 -120.7 21 0.333 -132.4 -137.7 351 6.9 99 S 73.7 0.015 -173.2 0.333 -109.4 -114.2 57.4 0.333 -119.5 -121.8 21.8 0.333 -133.5 -138.8 360.5 9.1 100 S 76.3 0.014 -173.5 0.333 -110.3 -115.2 57.9 0.333 -120.5 -122.8 25.1 0.333 -134.4 -139.8 339.8 5.6 101 S 87.8 0.012 -173.6 0.333 -111.2 -116.1 59.3 0.333 -121.5 -123.8 26.5 0.333 -135.2 -140.7 337.7 6.2 102 S 73.8 0.015 -173.4 0.333 -112.1 -117 60.7 0.333 -122.4 -124.8 19.7 0.333 -136 -141.5 343.7 6.1 103 S 77.8 0.013 -173.5 0.333 -113.1 -118 65 0.333 -123.5 -125.9 43.1 0.333 -136.8 -142.3 337.1 6.1 104 S 84.3 0.005 -173.3 0.333 -114.2 -119.1 73.9 0.333 -124.9 -127.2 85 0.333 -137.7 -143.1 355.2 8.1 105 S 66.2 0.006 -173 0.333 -115.4 -120.2 53.8 0.333 -130.4 -130.2 247.1 0.333 -156.2 -159.2 3024.4 9.0 106 I 66 0.005 -173.5 0.333 -117 -121.3 67.3 0.333 -135.6 -136.8 332.6 0.333 -165.3 -168 5193.7 7.0 107 I 75.1 0.004 -173.6 0.333 -119.3 -122.8 72.7 0.333 -141.2 -143.3 717.2 0.333 -164.4 -169.4 4979.8 12.3 108 I 77 0.004 -173.5 -124.6 -148.8 -169.7 6.2 109 I 81.3 0.004 -173.4 -126.9 -153.1 -169.8 7.3 110 I 78.1 0.004 -173.2 -129.4 -156.1 -169.9 6.2 111 I 78.5 0.003 -173.3 -132.2 -157.7 -169.8 7.3 112 I 78.4 0.003 -173.1 -134.9 -159.2 -169.9 11.1 113 I 79.4 0.003 -173.2 -137.5 -159.6 -169.8 11.2 114
114
EXP 3 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 76.7 0.003 -173.2 -139.9 -162 -169.9 8.8 115 I 77.2 0.002 -173.3 -142.2 -162.4 -170 6.9 116 I 83.1 0.002 -173.3 -144.3 -163.4 -170 7.2 117 I 82.1 0.002 -173.1 -146.3 -164.3 -170.1 8.5 118 I 82.3 0.002 -173 -148.2 -165.2 -170 11.8 119 I 75.7 0.002 -173.1 -150 -165.6 -170 8.7 120 I 78.4 0.001 -173.4 -151.7 -165.7 -170 12.3 121 I 80.2 0.001 -173.5 -153 -165.5 -170.2 8.2 122 I 88.7 0.001 -173.5 -154.2 -167.1 -170.4 8.7 123 I 87.3 0 -173.3 -155.9 -167.6 -170.4 12.2 124 I 83.9 0 -173.3 -157.3 -167.8 -170.4 12.2 125 I 86.6 0 -173.6 -158.8 -168.2 -170.3 12.4 126 I 90.5 0 -173.6 -159.7 -168.5 -170.5 9.0 127 I 89.6 0 -173.6 -160.5 -168.8 -170.6 12.4 128 I 96.2 0 -173.7 -161.2 -169 -170.6 12.1 129 I 97.1 0 -173.5 -161.7 -168.8 -170.7 12.2 130 I 98.6 0 -173.5 -162.1 -169 -170.6 12.2 131 I 91 0 -173.4 -162.4 -168.7 -170.6 11.9 132 I 96.4 0 -173.5 -162.8 -169 -170.5 12.2 133 I 91 0 -173.5 -163.1 -169.1 -170.6 12.3 134 I 95.4 0 -173.6 -163.4 -169.1 -170.6 12.4 135 I 98.1 0 -173.6 -163.6 -169.3 -170.7 12.4 136 I 94.7 0 -173.5 -164.1 -169.4 -170.7 12.0 137 I 92 0 -173.7 -164.4 -169.5 -170.8 12.4 138 I 95.3 0 -173.9 -164.7 -169.7 -170.9 11.6 139 I 96 0 -173.9 -165 -169.8 -171 12.3 140 I 94.5 0 -174 -166.3 -169.9 -171.1 12.4 141 I 100.3 0 -174.1 -167.3 -170.2 -171.2 12.4 142 I 99 0 -174.2 -167.6 -170.4 -171.3 12.4 143 I 102.1 0 -174.2 -168.1 -170.5 -171.4 12.3 144 I 104.8 0 -174.3 -168 -170.6 -171.5 11.8 145 I 104.7 0 -174.4 -168 -170.7 -171.5 12.0 146 I 106.2 0 -174.5 -167.8 -170.7 -171.6 11.9 147 I 104.8 0 -174.4 -167.5 -170.6 -171.6 11.6 148 I 106.2 0 -174.5 -167.3 -170.5 -171.6 12.0 149 I 106.5 0 -174.5 -167.8 -170.6 -171.7 12.4 150 I 110.8 0 -174.5 -169.2 -170.8 -171.8 12.2 151 I 110.9 0 -174.8 -170 -170.9 -171.8 12.4 152
115
EXP 3 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 109.5 0 -174.7 -170 -171 -171.9 12.1 153 I 107.1 0 -174.7 -170 -171 -172 12.4 154 I 102.3 0 -174.8 -170.2 -171 -172 12.4 155 I 112.1 0 -174.8 -170.2 -171.1 -172 11.5 156 I 129.8 0 -174.9 -170.2 -171.1 -172.1 12.1 157 I 121.4 0 -174.9 -170 -171.2 -172.2 11.9 158 I 124.1 0 -175.1 -169.7 -171.2 -172.3 12.3 159 I 122.7 0 -175.3 -169.6 -171.3 -172.5 12.4 160 I 123.7 0 -175.5 -169.5 -171.5 -172.7 12.4 161
EXP 4 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 0.3 1 17.4 0.333 23 24.1 245 0.333 22.9 24.1 216.9 0.333 22.1 23.3 432.4 0.0 1 N 8.3 1 17.4 0.333 22.1 24 74.1 0.333 22.2 24 51.5 0.333 21.3 23.3 77.5 0.0 2 N 69.3 1 17 0.333 18.2 24 192 0.333 17.9 24 177.9 0.333 15.6 23.2 285.2 0.0 3 S 95.4 1 -8.5 0.333 13.8 23 188.2 0.333 12.8 23.1 186.6 0.333 8.5 22.1 316.1 0.2 4 N 112.6 1 -73.7 0.333 9.5 19.7 166.7 0.333 7.6 19.8 170.7 0.333 1 17.4 322.9 0.0 5 S 123.8 0.234 -109.1 0.333 4.8 15.4 183.4 0.333 1.6 15.1 200 0.333 -7.4 10.6 380.3 0.4 6 S 137.4 0.168 -145.9 0.333 -0.4 11.1 200.1 0.333 -5.4 10 249 0.333 -15.6 2.9 397.6 0.3 7 S 167.2 0.136 -170.5 0.333 -5.7 6.3 205.5 0.333 -12.1 4.1 254.1 0.333 -23.5 -5.8 412.3 0.6 8 N 170.8 0.12 -170 0.333 -11.4 1.2 224.5 0.333 -19 -2.7 271.6 0.333 -30.8 -14.4 402.4 0.0 9 N 184.4 0.11 -169.9 0.333 -16.8 -4 221 0.333 -25.3 -9.6 265 0.333 -37.7 -22.9 397.2 0.0 10 S 183.4 0.098 -170.2 0.333 -21.6 -9.6 201.1 0.333 -31 -16.6 245 0.333 -44.2 -30.7 404 0.5 11 N 181.2 0.088 -170.5 0.333 -26.8 -15.2 217.7 0.333 -36.9 -23.2 258.5 0.333 -50.6 -38 410.1 0.0 12 N 187.6 0.082 -170.6 0.333 -31.5 -20.3 203.1 0.333 -42 -29.3 228.4 0.333 -56.2 -45 391.9 0.0 13 S 226.1 0.079 -170 0.333 -35.7 -25.6 185 0.333 -46.8 -35.3 223.3 0.333 -61.6 -51.7 399.7 3.7 14 N 235.2 0.076 -170.4 0.333 -40.2 -30.6 193.8 0.333 -51.6 -40.7 223.7 0.333 -66.8 -57.8 397.9 0.0 15 S 203.4 0.066 -171.1 0.333 -44.5 -35.1 190.4 0.333 -56.3 -45.8 224.8 0.333 -71.6 -63.6 392.9 4.0 16 N 218.9 0.063 -170.1 0.333 -48.4 -39.7 177.3 0.333 -60.8 -50.8 229.9 0.333 -76.3 -69 405.9 0.0 17 S 224.2 0.066 -170.7 0.333 -52.8 -44.1 200.9 0.333 -65.2 -55.6 221.3 0.333 -80.6 -74.1 391.2 2.5 18 S 206.4 0.055 -170.9 0.333 -56.8 -48.3 197.3 0.333 -69.4 -60.3 227.4 0.333 -85 -79.1 414.8 1.4 19 S 226.9 0.062 -169.8 0.333 -61 -52.8 201.5 0.333 -73.5 -64.8 221.7 0.333 -89 -83.6 399.5 3.7 20 S 216.9 0.052 -171.3 0.333 -65.1 -57.1 210.5 0.333 -77.7 -69.2 241.4 0.333 -92.6 -88.1 388.4 2.5 21 S 209.6 0.055 -169.6 0.333 -68.7 -61.4 189.8 0.333 -81.4 -73.5 214.4 0.333 -96.4 -92.3 411 4.6 22 S 221.6 0.05 -171.5 0.333 -72.6 -65.7 208.4 0.333 -85.1 -77.8 226.3 0.333 -99.8 -96.1 399 3.3 23 S 196.5 0.055 -169.7 0.333 -75.6 -69.7 170.3 0.333 -88.2 -81.7 187.4 0.333 -103.4 -100 433 5.0 24
116
EXP 4 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t S 258 0.051 -172 0.333 -79.2 -73.8 199.4 0.333 -91.7 -85.5 226.6 0.333 -106.3 -103.5 401 4.3 25 S 208.2 0.053 -169.9 0.333 -82.6 -77.2 192.6 0.333 -95.2 -88.9 224.7 0.333 -109.4 -107.2 412.6 3.4 26 S 259.9 0.051 -170.9 0.333 -86.1 -80.9 210.2 0.333 -98.4 -92.5 228.6 0.333 -112.1 -110.3 399 4.9 27 S 192.4 0.054 -170 0.333 -88.9 -84.5 178.4 0.333 -101.5 -96 222.6 0.333 -115.2 -113.5 441.6 5.0 28 S 262.3 0.053 -171.7 0.333 -92 -88.1 196.6 0.333 -104.3 -99.4 216.8 0.333 -117.7 -116.2 418 3.8 29 S 213 0.054 -170.3 0.333 -94.9 -91.3 186.6 0.333 -107 -102.6 200.9 0.333 -120.6 -119.3 453.3 2.9 30 S 257.1 0.052 -171.2 0.333 -97.8 -94.5 200 0.333 -109.8 -105.6 221.3 0.333 -122.6 -121.9 406.5 5.9 31 S 200.2 0.057 -170 0.333 -100.6 -97.6 201.3 0.333 -112.5 -108.4 219.6 0.333 -125.1 -124.8 442.7 4.0 32 S 247.8 0.05 -171.5 0.333 -103 -100.7 175.5 0.333 -114.8 -111.2 211.1 0.333 -127.1 -127 428.8 1.5 33 S 198.6 0.054 -169.9 0.333 -105.9 -103.8 213 0.333 -117.6 -114 246.9 0.333 -129.3 -129.4 457.6 6.7 34 S 220.2 0.051 -171.2 0.333 -108.4 -106.4 195.1 0.333 -120.1 -116.5 237 0.333 -131.8 -131.6 484.2 4.3 35 S 222.7 0.051 -170.6 0.333 -110.6 -109.3 180.7 0.333 -122.1 -119.3 205.9 0.333 -133.3 -133.7 428.1 1.1 36 S 221.7 0.052 -169.9 0.333 -112.8 -112.1 183.1 0.333 -124.4 -121.9 240.8 0.333 -135.5 -136.1 503.7 7.6 37 S 204.3 0.046 -171.8 0.333 -114.7 -114.5 147.3 0.333 -126.7 -124.1 252.4 0.333 -137.8 -137.9 543.1 7.4 38 S 238.2 0.046 -170.6 0.333 -117 -116.9 192.4 0.333 -128.7 -126.4 242.3 0.333 -139.6 -139.9 537.9 4.7 39 S 218.3 0.047 -170 0.333 -121.2 -118.9 158.2 0.333 -144.9 -128.8 1963 0.333 -160.1 -142.2 3521.3 9.5 40 S 209.2 0.042 -171.7 0.333 -126.9 -121.2 167.6 0.333 -160.7 -130.9 4628.5 0.333 -163.4 -144.1 3866.8 5.2 41 S 234.1 0.034 -170.4 0.333 -132.6 -123.7 437.5 0.333 -161 -144 4509.1 0.333 -164 -160.1 3413.6 8.6 42 S 199.5 0.036 -169.7 0.333 -138 -126.9 539.4 0.333 -162.2 -160.7 3671.7 0.333 -165.1 -165.1 3074.8 7.9 43 S 198.5 0.034 -173.1 -132.4 -163.8 -167.6 9.5 44 S 201.3 0.036 -171 -138.5 -165.7 -168.8 8.3 45 S 209 0.036 -170.5 -145 -165.9 -167.7 3.7 46 S 209.6 0.033 -171 -150.6 -166.3 -167.3 9.1 47 S 209.5 0.033 -171.2 -160.3 -166.6 -167.6 5.9 48 S 213.6 0.032 -171.4 -165.5 -166.9 -167.9 4.0 49 S 214.4 0.031 -171.7 -166.2 -167.3 -168.2 7.9 50 S 219 0.03 -172.2 -166.4 -167.6 -168.6 8.6 51 S 227.3 0.028 -172.6 -166.7 -168.1 -169.1 4.6 52 S 229.7 0.027 -172.9 -166.9 -168.5 -169.7 5.1 53 S 236.5 0.026 -173.2 -167.2 -169 -170.1 6.9 54 S 244.6 0.025 -173.5 -167.5 -169.4 -170.5 7.0 55 S 247.6 0.024 -173.7 -167.7 -169.8 -170.9 5.6 56 S 245.4 0.023 -174 -168 -170.1 -171.2 5.3 57 I 247.2 0.022 -174.2 -168.2 -170.3 -171.5 7.7 58 I 251.8 0.021 -174.3 -168.4 -170.5 -171.8 8.8 59 I 254.8 0.02 -174.9 -168.7 -170.8 -172.1 11.0 60 I 254.5 0.02 -175.5 -169.3 -171.4 -172.8 7.0 61 I 257.6 0.019 -176.1 -169.9 -172 -173.4 3.7 62
117
EXP 4 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 261.3 0.018 -176.8 -170.4 -172.5 -174 4.3 63 I 261.7 0.017 -177.2 -170.9 -172.9 -174.4 6.4 64 I 262.1 0.016 -177.8 -171.3 -173.3 -174.8 8.1 65 I 261.9 0.015 -178 -171.7 -173.7 -175.3 8.9 66 I 263 0.015 -178.1 -171.8 -173.9 -175.5 5.5 67 I 260.5 0.014 -178.1 -171.9 -173.9 -175.5 4.9 68 I 260.2 0.013 -178.2 -172.1 -174.1 -175.8 8.4 69 I 261.8 0.013 -178.5 -172.3 -174.2 -176 7.7 70 I 260.4 0.012 -178.7 -172.5 -174.5 -176.2 8.1 71 I 261.9 0.011 -178.8 -172.6 -174.7 -176.5 6.8 72 I 262.3 0.011 -179.3 -173 -174.8 -176.6 4.0 73 I 264 0.01 -179.7 -173.5 -175.1 -177 11.6 74 I 264.7 0.01 -179.8 -173.9 -175.4 -177.3 7.8 75 I 261.4 0.009 -180.4 -174.5 -175.9 -177.8 9.4 76 I 260.1 0.009 -180.7 -174.9 -176.3 -178.3 8.7 77 I 261.5 0.008 -180.9 -174.9 -176.4 -178.3 9.2 78 I 261.5 0.008 -181 -175.2 -176.6 -178.6 7.4 79 I 261.7 0.007 -181.3 -175.3 -176.9 -178.9 9.1 80 I 259.6 0.007 -181.6 -175.5 -177 -179.1 10.7 81 I 258.5 0.007 -181.7 -175.7 -177.2 -179.4 11.7 82 I 260.3 0.006 -181.9 -176 -177.4 -179.6 10.2 83 I 260 0.006 -182 -176.3 -177.5 -179.7 10.8 84 I 257.6 0.005 -182.4 -176.8 -178 -180.2 11.0 85 I 255.4 0.005 -183.3 -177.7 -178.8 -181 9.4 86 I 256.3 0.005 -184.3 -178.7 -179.8 -182.2 10.1 87 I 255.6 0.004 -185.3 -179.8 -180.9 -183.2 11.2 88 I 254.6 0.004 -185.8 -180.4 -181.4 -183.8 11.2 89 I 252.9 0.004 -185.8 -180.4 -181.5 -183.9 10.5 90 I 254 0.003 -185.7 -180.4 -181.4 -183.8 12.1 91 I 254.6 0.003 -185.5 -180.3 -181.3 -183.7 11.2 92 I 253.1 0.003 -185.3 -180.1 -181.1 -183.5 11.2 93 I 253.3 0.002 -185.4 -180.3 -181.3 -183.7 11.7 94 I 251.6 0.002 -185.5 -180.3 -181.4 -183.8 11.9 95 I 251.4 0.002 -185.4 -180.3 -181.4 -183.8 11.2 96 I 249.5 0.002 -185.4 -180.3 -181.3 -183.7 11.5 97 I 247.5 0.001 -185.2 -180.1 -181.2 -183.7 11.9 98 I 247.3 0.001 -185.2 -180.1 -181.2 -183.7 11.6 99 I 245.7 0.001 -185.2 -180.1 -181.2 -183.8 10.3 100
118
EXP 5 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 110.9 1 12.8 0.333 24.2 24.8 48 0.333 24 24.8 11.6 0.333 22.5 23.5 452.4 0.0 1 N 149.1 1 -3 0.333 22.9 23.8 186.5 0.333 22.8 23.8 148.5 0.333 21.6 22.3 191.2 0.0 2 N 178 1 -19.4 0.333 20.5 21.6 257.3 0.333 20.5 21.9 205.3 0.333 19.1 20.2 275.5 0.0 3 N 199.3 1 -39.9 0.333 17.1 18.4 217.4 0.333 17.2 18.9 178.9 0.333 15.5 16.8 238.5 0.0 4 S 207.3 0.15 -88.7 0.333 12.4 13.9 204.1 0.333 12.5 14.6 179.9 0.333 10.1 11.8 234.3 1.2 5 N 209.9 0.128 -144.8 0.333 7 8.6 207.9 0.333 6.7 9.1 190.2 0.333 3.4 5.3 263.3 0.0 6 N 224.6 0.113 -173.5 0.333 0.7 2.3 249.6 0.333 -0.1 2.6 234.2 0.333 -4.8 -2.7 335.7 0.0 7 N 232.7 0.1 -173.7 0.333 -6.4 -4.8 287.5 0.333 -7.8 -4.9 276.6 0.333 -13.1 -11.2 363.8 0.0 8 N 231.9 0.09 -173.9 0.333 -13.1 -11.8 288.5 0.333 -15 -12.4 278.9 0.333 -21 -19.5 372.8 0.0 9 N 243.3 0.083 -174.2 0.333 -19.3 -18.3 277.9 0.333 -21.9 -19.6 275.7 0.333 -28.4 -27.3 369.3 0.0 10 N 243 0.077 -174.4 0.333 -25.4 -24.8 279.5 0.333 -28.7 -26.6 280 0.333 -35.6 -34.9 372 0.0 11 N 251.9 0.072 -174.6 0.333 -31.1 -30.8 268.6 0.333 -35.1 -33.3 274.8 0.333 -42.2 -41.9 361.7 0.0 12 N 256.9 0.068 -174.8 0.333 -36.8 -36.7 269.1 0.333 -41.3 -39.7 278.3 0.333 -48.7 -48.7 367.7 0.0 13 S 265.9 0.065 -174.9 0.333 -42 -42.2 255.6 0.333 -47.2 -45.9 272.1 0.333 -54.6 -54.9 355.9 0.5 14 S 271.4 0.062 -175 0.333 -47.1 -47.6 254.4 0.333 -52.7 -51.7 270.2 0.333 -60.2 -60.9 352.4 1.0 15 S 277.6 0.06 -175.1 0.333 -51.9 -52.7 248.8 0.333 -58.1 -57.3 269.4 0.333 -65.4 -66.3 336.8 1.1 16 S 287 0.058 -175.2 0.333 -56.6 -57.6 244.8 0.333 -63.1 -62.6 270.7 0.333 -69.7 -70.9 299.9 1.2 17 S 290.5 0.056 -175.4 0.333 -61.1 -62.3 238.9 0.333 -67.8 -67.5 263.4 0.333 -74.4 -75.6 319.9 1.0 18 S 299.9 0.055 -175.5 0.333 -65.4 -66.8 234 0.333 -72.3 -72.2 259.6 0.333 -78.8 -80.2 318.5 0.4 19 S 305.7 0.055 -175.8 0.333 -69.3 -71 222.4 0.333 -76.4 -76.6 249.3 0.333 -82.8 -84.4 306.7 0.7 20 S 323.9 0.057 -175.6 0.333 -73 -75 217.5 0.333 -80.3 -80.7 241.8 0.333 -86.7 -88.5 307.5 1.0 21 S 352.5 0.058 -175.3 0.333 -76.5 -78.8 210.7 0.333 -83.9 -84.4 228.9 0.333 -90.4 -92.3 302.5 1.5 22 S 376.1 0.059 -175.1 0.333 -80 -82.4 208.2 0.333 -87.4 -88.1 235.5 0.333 -93.8 -95.9 298.5 2.7 23 S 390.3 0.059 -175 0.333 -83.4 -86 212.6 0.333 -91 -91.8 242.1 0.333 -97.2 -99.3 298 4.0 24
SW 374.9 0.059 -175.3 0.333 -86.8 -89.6 217.8 0.333 -94.5 -95.4 247.7 0.333 -100.5 -102.7 305.9 4.4 25 SW 362.3 0.062 -175.3 0.333 -90 -93 213.9 0.333 -97.7 -98.8 241.9 0.333 -103.7 -106 302 4.4 26 SW 407.9 0.065 -175.6 0.333 -93.1 -96.3 211.2 0.333 -100.8 -102 237.9 0.333 -106.7 -109.1 300.9 4.6 27 SW 390.9 0.066 -175.7 0.333 -95.9 -99.4 201 0.333 -103.7 -105 229.5 0.333 -109.5 -112 293.7 5.4 28 SW 414.4 0.067 -175.9 0.333 -98.8 -102.4 201.9 0.333 -106.5 -108 230.8 0.333 -112.2 -114.8 294.6 4.6 29 SW 387.5 0.067 -176.2 0.333 -101.4 -105.2 194.6 0.333 -109.1 -110.7 220.7 0.333 -114.7 -117.5 290.3 4.1 30 SW 394.5 0.068 -176.2 0.333 -103.8 -107.8 185.9 0.333 -111.5 -113.2 210.5 0.333 -117.2 -120 289.1 6.1 31 SW 376 0.066 -176.6 0.333 -106.2 -110.4 184.9 0.333 -114 -115.7 213.8 0.333 -119.6 -122.5 293.3 5.8 32 SW 368.6 0.065 -176.7 0.333 -108.5 -112.8 180.1 0.333 -116.3 -118.1 211.8 0.333 -121.8 -124.9 287.6 5.7 33 SW 354.8 0.063 -176.9 0.333 -110.6 -115.1 177 0.333 -118.4 -120.4 207.5 0.333 -123.9 -127 281.3 6.9 34 SW 342.5 0.061 -177.1 0.333 -112.6 -117.3 169.5 0.333 -120.4 -122.5 198.6 0.333 -125.9 -129.1 280.6 3.7 35 SW 334.5 0.06 -177.2 0.333 -114.7 -119.4 172.4 0.333 -122.5 -124.6 202.9 0.333 -127.8 -131.1 284.6 5.1 36 SW 329 0.06 -177.2 0.333 -116.7 -121.5 176.8 0.333 -124.5 -126.7 210 0.333 -129.8 -133.1 293.2 4.7 37 SW 328.7 0.058 -177.2 0.333 -118.8 -123.7 191.8 0.333 -126.5 -128.8 220.3 0.333 -131.7 -135 291.1 4.4 38
119
EXP 5 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 328.7 0.056 -177.3 0.333 -120.7 -125.8 183.9 0.333 -128.5 -130.8 216.5 0.333 -133.6 -137 305.3 4.3 39 SW 326.2 0.055 -177.5 0.333 -122.5 -127.7 173.5 0.333 -130.2 -132.6 202 0.333 -135.2 -138.7 291.3 12.4 40 SW 323.3 0.053 -177.6 0.333 -124.2 -129.6 170.1 0.333 -131.9 -134.4 213.2 0.333 -136.9 -140.4 293.2 11.7 41 SW 324 0.052 -177.7 0.333 -125.9 -131.3 172.5 0.333 -133.6 -136.2 208.3 0.333 -138.5 -142.1 302 3.4 42 SW 327.9 0.05 -177.9 0.333 -127.4 -133 165.4 0.333 -135.2 -137.8 211.1 0.333 -140 -143.6 295.4 3.3 43 SW 331.3 0.049 -177.8 0.333 -129 -134.7 171.1 0.333 -136.8 -139.4 212.7 0.333 -141.3 -145 284.1 5.3 44 SW 324.2 0.026 -177.8 0.333 -130.6 -136.4 181.1 0.333 -138.5 -141.1 214.3 0.333 -144.2 -147.6 499.4 6.4 45 SW 319.9 0.011 -177.7 0.333 -133.3 -138.1 152.3 0.333 -149.6 -149.8 1248 0.333 -164.4 -164.4 3141.8 8.3 46 SW 309.6 0.019 -177.8 0.333 -136.9 -139.6 30.1 0.333 -164.5 -164.8 3462.8 0.333 -170 -171.5 3628.1 7.1 47 SW 302.3 0.014 -178 0.333 -139.6 -141.6 47.1 0.333 -166.9 -169.8 3562.7 0.333 -169 -172.8 1152.9 7.9 48 SW 294.5 0.044 -178.2 0.333 24.2 -145.3 0.333 24 -171.4 0.333 22.5 -173.3 5.9 49 SW 285.1 0.043 -178.5 0.333 22.9 -152.5 0.333 22.8 -172.2 0.333 21.6 -173.8 5.7 50 SW 281.6 0.043 -178.7 0.333 20.5 -166.3 0.333 20.5 -172.7 0.333 19.1 -174.1 5.2 51 SW 275.5 0.042 -178.9 0.333 17.1 -171.7 0.333 17.2 -173.2 0.333 15.5 -174.5 3.0 52 SW 275.3 0.041 -179.1 0.333 12.4 -172.7 0.333 12.5 -173.5 0.333 10.1 -174.8 3.6 53 SW 266.4 0.041 -179.1 0.333 7 -172.9 0.333 6.7 -173.7 0.333 3.4 -174.9 4.8 54 SW 270.3 0.04 -179.4 0.333 0.7 -173.1 0.333 -0.1 -173.8 0.333 -4.8 -175 4.5 55 SW 267.6 0.039 -179.2 0.333 -6.4 -173.3 0.333 -7.8 -173.9 0.333 -13.1 -175.2 6.2 56 SW 263.7 0.038 -179.3 0.333 -13.1 -173.4 0.333 -15 -174 0.333 -21 -175.3 5.8 57 SW 267.1 0.037 -179.2 0.333 -19.3 -173.4 0.333 -21.9 -174 0.333 -28.4 -175.3 6.4 58 SW 264.7 0.037 -179 0.333 -25.4 -173.4 0.333 -28.7 -174 0.333 -35.6 -175.4 8.3 59 SW 263.3 0.035 -179.1 0.333 -31.1 -173.4 0.333 -35.1 -174 0.333 -42.2 -175.4 9.2 60 SW 262.4 0.034 -179.1 0.333 -36.8 -173.5 0.333 -41.3 -174 0.333 -48.7 -175.4 5.5 61 SW 259.9 0.034 -179.1 0.333 -42 -173.5 0.333 -47.2 -174 0.333 -54.6 -175.4 12.4 62
I 255.6 0.033 -179.2 0.333 -47.1 -173.5 0.333 -52.7 -174.1 0.333 -60.2 -175.5 4.8 63 I 253.6 0.033 -179.3 0.333 -51.9 -173.6 0.333 -58.1 -174.2 0.333 -65.4 -175.6 3.7 64 I 252.2 0.032 -179.4 0.333 -56.6 -173.7 0.333 -63.1 -174.3 0.333 -69.7 -175.8 3.5 65 I 252.2 0.031 -179.6 0.333 -61.1 -173.9 0.333 -67.8 -174.5 0.333 -74.4 -175.9 4.5 66 I 249.9 0.031 -179.7 0.333 -65.4 -174.1 0.333 -72.3 -174.6 0.333 -78.8 -176.1 6.0 67 I 245.5 0.031 -179.8 0.333 -69.3 -174.2 0.333 -76.4 -174.7 0.333 -82.8 -176.3 7.9 68 I 248.6 0.03 -180 0.333 -73 -174.4 0.333 -80.3 -174.9 0.333 -86.7 -176.5 4.6 69 I 247.8 0.03 -180.1 0.333 -76.5 -174.6 0.333 -83.9 -175 0.333 -90.4 -176.7 5.4 70 I 246.1 0.029 -180.3 0.333 -80 -174.7 0.333 -87.4 -175.2 0.333 -93.8 -176.8 8.2 71 I 245.9 0.029 -180.4 0.333 -83.4 -174.8 0.333 -91 -175.3 0.333 -97.2 -177 12.4 72 I 246.1 0.028 -180.5 0.333 -86.8 -174.9 0.333 -94.5 -175.4 0.333 -100.5 -177.1 12.4 73 I 242.4 0.028 -180.7 0.333 -90 -175.1 0.333 -97.7 -175.5 0.333 -103.7 -177.2 8.4 74 I 240 0.027 -180.9 0.333 -93.1 -175.2 0.333 -100.8 -175.7 0.333 -106.7 -177.5 12.4 75 I 239.5 0.027 -181 0.333 -95.9 -175.4 0.333 -103.7 -175.9 0.333 -109.5 -177.7 6.2 76
120
EXP 5 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 240.5 0.026 -181.1 0.333 -98.8 -175.5 0.333 -106.5 -176 0.333 -112.2 -177.8 6.6 77 I 240.8 0.026 -181.1 0.333 -101.4 -175.5 0.333 -109.1 -176 0.333 -114.7 -177.8 4.2 78 I 235 0.026 -181.1 0.333 -103.8 -175.5 0.333 -111.5 -176 0.333 -117.2 -177.9 5.7 79 I 238.7 0.025 -181.1 0.333 -106.2 -175.5 0.333 -114 -176.1 0.333 -119.6 -177.9 6.7 80 I 241.3 0.024 -181.1 0.333 -108.5 -175.6 0.333 -116.3 -176 0.333 -121.8 -177.9 7.1 81 I 238.7 0.024 -181.1 0.333 -110.6 -175.6 0.333 -118.4 -176.1 0.333 -123.9 -177.9 5.8 82 I 237.2 0.024 -181.2 0.333 -112.6 -175.6 0.333 -120.4 -176.1 0.333 -125.9 -178 4.3 83 I 237.7 0.023 -181.3 0.333 -114.7 -175.6 0.333 -122.5 -176.1 0.333 -127.8 -178 4.5 84 I 238.2 0.023 -181.3 0.333 -116.7 -175.6 0.333 -124.5 -176.2 0.333 -129.8 -178.1 5.1 85 I 238.4 0.022 -181.3 0.333 -118.8 -175.6 0.333 -126.5 -176.2 0.333 -131.7 -178.1 4.1 86 I 237.9 0.022 -181.4 0.333 -120.7 -175.7 0.333 -128.5 -176.2 0.333 -133.6 -178.2 6.4 87 I 237.5 0.022 -181.4 0.333 -122.5 -175.8 0.333 -130.2 -176.3 0.333 -135.2 -178.3 5.4 88 I 235.3 0.021 -181.5 0.333 -124.2 -175.8 0.333 -131.9 -176.3 0.333 -136.9 -178.4 5.2 89 I 233.2 0.021 -181.6 0.333 -125.9 -175.9 0.333 -133.6 -176.4 0.333 -138.5 -178.5 7.6 90 I 233.7 0.021 -181.7 0.333 -127.4 -176 0.333 -135.2 -176.5 0.333 -140 -178.7 4.4 91 I 231.4 0.02 -182 0.333 -129 -176.2 0.333 -136.8 -176.7 0.333 -141.3 -178.9 4.4 92 I 231.7 0.02 -182.1 -176.4 -176.9 -179.2 6.3 93 I 231.1 0.02 -182.4 -176.6 -177 -179.4 4.5 94 I 231.5 0.019 -182.9 -177.1 -177.5 -179.9 5.1 95 I 230.1 0.019 -183.5 -177.7 -178.2 -180.6 5.0 96 I 230.9 0.019 -184.1 -178.3 -178.7 -181.2 4.6 97 I 230.6 0.018 -184.4 -178.7 -179.1 -181.6 6.7 98 I 229.9 0.018 -184.6 -178.9 -179.3 -181.9 6.2 99 I 228.4 0.018 -184.9 -179 -179.5 -182.1 6.5 100 I 231.1 0.017 -184.9 -179.2 -179.7 -182.1 12.4 101 I 227.8 0.017 -184.9 -179.1 -179.7 -182.2 5.6 102 I 228.1 0.017 -184.9 -179.1 -179.6 -182.2 3.9 103 I 228.1 0.017 -184.9 -179.2 -179.7 -182.2 3.7 104 I 226.2 0.016 -184.9 -179.2 -179.7 -182.3 6.4 105 I 224.4 0.016 -185.1 -179.4 -179.9 -182.5 7.3 106 I 225.4 0.016 -185.2 -179.5 -180.1 -182.7 5.7 107 I 225.5 0.016 -185.3 -179.6 -180.2 -182.8 10.0 108 I 222.3 0.015 -185.3 -179.7 -180.3 -182.9 9.6 109 I 223.5 0.015 -185.5 -179.8 -180.3 -183 10.5 110 I 223.9 0.015 -185.5 -179.8 -180.3 -183.1 12.4 111 I 222.1 0.015 -185.6 -179.8 -180.4 -183.2 8.2 112 I 220.6 0.015 -185.7 -180 -180.5 -183.4 10.2 113
121
EXP 6 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 123.3 1 -11.1 0.333 21.5 22.8 206.5 0.333 21.4 22.9 175 0.333 20 21.6 314.2 0.0 1 N 140.4 1 -61.5 0.333 18.6 19.9 166 0.333 18.6 20.2 143.7 0.333 17.2 18.5 176.2 0.0 2 N 157.6 1 -104.8 0.333 14.4 16 165.3 0.333 14.1 16.1 157.7 0.333 11.8 13.6 217.2 0.0 3 N 171.1 0.595 -154.4 0.333 10.3 11.7 161.7 0.333 9.4 11.5 160.9 0.333 5.9 7.7 237.6 0.0 4 N 180.7 0.354 -172.8 0.333 5.9 7.3 171.2 0.333 4.3 6.5 172.3 0.333 -0.8 0.9 280.7 0.0 5 N 197.5 0.265 -173 0.333 1.1 2.5 187 0.333 -1.6 0.8 206.3 0.333 -7.8 -6.4 312.9 0.0 6 N 191.9 0.217 -173 0.333 -3.9 -2.5 197.4 0.333 -7.5 -5.3 222.6 0.333 -14.3 -13.2 306.9 0.0 7
SW 195.6 0.185 -173 0.333 -8.3 -7.2 182.3 0.333 -12.9 -10.9 209.7 0.333 -20.5 -19.9 309.5 1.3 8 SW 229.7 0.162 -172.9 0.333 -13.1 -12 194.2 0.333 -18.5 -16.6 221.6 0.333 -26.8 -26.4 320.9 2.7 9 SW 224.3 0.143 -173.1 0.333 -17.3 -16.5 177.6 0.333 -23.5 -21.9 209.9 0.333 -32.1 -32.3 299.7 2.9 10 SW 221.8 0.128 -173.2 0.333 -21.7 -21 183 0.333 -28.5 -27.1 209.9 0.333 -37.5 -37.9 300.8 2.3 11 SW 220.5 0.113 -173.3 0.333 -26.1 -25.5 184.6 0.333 -33.4 -32.2 216.3 0.333 -42.6 -43.2 297.6 2.4 12 SW 230.7 0.106 -173.5 0.333 -30.6 -30.1 190.9 0.333 -38.2 -37.2 215.5 0.333 -47.6 -48.5 306.4 2.5 13 SW 236.7 0.101 -173.5 0.333 -34.3 -34.1 166.2 0.333 -42.4 -41.7 196.1 0.333 -52.3 -53.4 299.6 0.0 14 SW 257.4 0.094 -173.5 0.333 -38.5 -38.4 180.6 0.333 -47 -46.3 212.3 0.333 -57 -58.3 307.9 0.0 15 SW 227.9 0.087 -173.8 0.333 -42.5 -42.6 180.3 0.333 -51.5 -50.9 219.8 0.333 -61.5 -63 309.7 4.5 16 SW 252.6 0.083 -173.4 0.333 -46.3 -46.5 174.3 0.333 -55.6 -55.2 208.9 0.333 -65.9 -67.6 313.6 4.1 17 SW 296.6 0.087 -173 0.333 -49.8 -50.3 165.6 0.333 -59.2 -59.1 186 0.333 -69.9 -71.9 303.8 2.8 18 SW 244 0.077 -174.1 0.333 -52.9 -53.7 144.8 0.333 -62.8 -62.8 187.5 0.333 -73.6 -75.8 298.1 6.3 19 SW 278.5 0.078 -173.1 0.333 -56.8 -57.6 183.4 0.333 -67 -66.8 202.8 0.333 -79.4 -81.3 421.7 2.0 20 SW 318 0.082 -173.2 0.333 -60.4 -61.4 178.2 0.333 -70.6 -70.7 198.3 0.333 -82.6 -85.2 314 3.5 21 SW 277.7 0.07 -174.2 0.333 -63.7 -64.9 167.6 0.333 -74.1 -74.4 195.9 0.333 -86.1 -88.9 322.4 0.0 22 SW 283.4 0.069 -172.9 0.333 -67.3 -68.6 181.2 0.333 -77.7 -78.1 198.4 0.333 -89.5 -92.5 328.6 2.7 23 SW 309.5 0.067 -173.5 0.333 -70.4 -72 170.1 0.333 -80.9 -81.4 188.1 0.333 -92.7 -95.8 324.4 0.0 24 SW 253.4 0.062 -173.2 0.333 -73.2 -75.1 150.8 0.333 -83.9 -84.6 181.6 0.333 -95.9 -99.1 333 3.2 25 SW 311.1 0.065 -173.4 0.333 -76.2 -78.2 161.5 0.333 -86.9 -87.8 185.7 0.333 -98.5 -101.9 303.4 0.0 26 SW 274 0.065 -172.7 0.333 -79.3 -81.4 168 0.333 -89.9 -90.8 187.6 0.333 -101.3 -104.8 314.8 3.9 27 SW 314.4 0.063 -173.7 0.333 -82.4 -84.7 181.5 0.333 -92.9 -93.9 196.7 0.333 -104.1 -107.6 321.2 3.3 28 SW 267.2 0.062 -173.2 0.333 -85.5 -87.9 182.5 0.333 -96.2 -97.2 217.7 0.333 -107.2 -110.6 353 2.7 29 SW 317.8 0.066 -173.5 0.333 -88.2 -90.9 170.1 0.333 -98.7 -99.9 178.4 0.333 -109.6 -113.2 326.7 5.0 30 SW 292.3 0.058 -173.6 0.333 -90.7 -93.6 157.2 0.333 -101.3 -102.6 187.2 0.333 -112.1 -115.8 341 4.3 31 SW 281 0.062 -172.6 0.333 -93.1 -96.2 155 0.333 -103.7 -105.1 176.6 0.333 -114.5 -118.3 335.4 5.1 32 SW 308.9 0.061 -173.1 0.333 -95.8 -99 173.6 0.333 -106.4 -107.8 199 0.333 -117.1 -120.8 360.6 4.0 33 SW 290 0.057 -173.3 0.333 -98.3 -101.6 169.4 0.333 -108.7 -110.3 186.3 0.333 -119 -123 323.5 2.9 34 SW 267.5 0.06 -172.7 0.333 -100.4 -104 146.2 0.333 -110.9 -112.6 180.6 0.333 -121.3 -125.2 352.4 5.1 35 SW 300.4 0.057 -173.3 0.333 -102.6 -106.3 158.1 0.333 -113.1 -114.9 188.4 0.333 -123.2 -127.2 342.4 3.5 36 SW 283.5 0.06 -172.1 0.333 -104.9 -108.7 165.4 0.333 -115.3 -117.1 183.9 0.333 -125.3 -129.3 356.6 4.3 37 SW 259.4 0.054 -173.9 0.333 -107.2 -111.1 170.1 0.333 -117.4 -119.3 197.6 0.333 -127 -131.1 331.7 4.1 38
122
EXP 6 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 289.9 0.055 -172.6 0.333 -109.2 -113.3 162.7 0.333 -119.4 -121.4 184.2 0.333 -128.9 -133 365.7 2.8 39 SW 276 0.054 -172.8 0.333 -111.1 -115.4 146.8 0.333 -121.2 -123.3 171.6 0.333 -130.8 -134.9 370.9 5.5 40 SW 277.6 0.048 -173.6 0.333 -113 -117.4 156.7 0.333 -123 -125.2 180.4 0.333 -132.4 -136.6 354.4 2.7 41 SW 299.1 0.048 -172.7 0.333 -114.8 -119.3 149.6 0.333 -124.8 -127 173.5 0.333 -134.1 -138.4 389.3 3.3 42 SW 283.7 0.047 -172.6 0.333 -116.5 -121.1 144.7 0.333 -126.5 -128.8 180.8 0.333 -135.7 -140 376 5.9 43 SW 286.1 0.043 -173.1 0.333 -118.1 -122.9 147 0.333 -128.1 -130.5 181.2 0.333 -137.1 -141.4 368 3.4 44 SW 291.8 0.042 -172.7 0.333 -119.8 -124.7 152.8 0.333 -129.7 -132.1 173.5 0.333 -138.4 -142.8 375.1 6.3 45 SW 282 0.042 -172.4 0.333 -121.3 -126.3 140.9 0.333 -131.2 -133.7 174.2 0.333 -139.9 -144.3 404.4 4.9 46 SW 265.6 0.013 -172.6 0.333 -123.1 -128.1 168.6 0.333 -133.6 -135.7 197.2 0.333 -146 -149.6 1170.9 8.1 47 SW 262.7 0.014 -173 0.333 -126.6 -129.8 101.2 0.333 -149.3 -148.7 2042.5 0.333 -164.1 -164.4 3757.5 7.8 48 SW 261.8 0.009 -172.5 0.333 -130.2 -131.6 16.2 0.333 -160.8 -161.7 3928.6 0.333 -164.7 -167.5 3199.4 8.8 49 SW 252.9 0.035 -172.6 -135 -165.6 -167.9 4.1 50 SW 255.8 0.033 -173 -141.1 -166.9 -168.4 4.4 51 SW 257.3 0.032 -172.8 -154.4 -167.4 -168.8 5.2 52 SW 250.4 0.032 -172.7 -164.8 -167.5 -168.9 4.6 53 SW 249.3 0.03 -172.9 -166.5 -167.6 -168.9 5.1 54 SW 251.5 0.029 -172.9 -166.8 -167.8 -169.1 5.0 55 SW 253.7 0.028 -173 -166.8 -167.9 -169.3 5.0 56 SW 252.5 0.027 -173.1 -167.1 -167.9 -169.4 5.8 57 SW 258.5 0.026 -173.2 -167.2 -168 -169.6 4.9 58 SW 265.1 0.024 -173.6 -167.4 -168.2 -169.8 4.7 59 SW 267.3 0.023 -173.7 -167.5 -168.4 -170.1 4.9 60 SW 271.2 0.022 -174 -167.6 -168.7 -170.4 5.3 61 SW 274.6 0.021 -174.3 -167.8 -168.9 -170.9 6.3 62 SW 277.8 0.02 -174.8 -168.2 -169.4 -171.4 6.1 63
I 283.2 0.019 -175.2 -168.6 -169.9 -171.9 12.4 64 I 292.6 0.019 -175.7 -169 -170.5 -172.4 12.4 65 I 300.9 0.018 -176.3 -169.4 -171 -173 7.3 66 I 304.8 0.017 -176.9 -169.9 -171.7 -173.6 6.6 67 I 308.1 0.016 -177.5 -170.6 -172.3 -174.3 7.7 68 I 308.4 0.016 -178 -171.1 -172.8 -174.7 7.7 69 I 310.1 0.015 -178.3 -171.4 -173.1 -175.1 6.7 70 I 313.1 0.014 -178.6 -171.7 -173.4 -175.5 7.1 71 I 317.1 0.013 -178.8 -171.9 -173.6 -175.7 7.8 72 I 320.9 0.013 -178.9 -172.1 -173.8 -175.9 8.8 73 I 323.6 0.012 -179 -172.2 -174 -176 12.4 74 I 326.8 0.011 -179.2 -172.4 -174.2 -176.2 8.1 75 I 330.5 0.01 -179.5 -172.6 -174.4 -176.5 6.2 76
123
EXP 6 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 332.7 0.01 -179.6 -172.8 -174.5 -176.6 9.6 77 I 335.4 0.009 -179.7 -173 -174.7 -176.8 10.0 78 I 338.1 0.009 -179.7 -173.2 -174.8 -176.9 12.4 79 I 339 0.008 -179.7 -173.2 -174.8 -177 12.4 80 I 339.4 0.008 -179.8 -173.4 -174.9 -177.2 12.4 81 I 340.9 0.007 -180.1 -173.7 -175.2 -177.5 10.1 82 I 340.8 0.006 -180.2 -174 -175.5 -177.7 9.0 83 I 343.4 0.006 -180.3 -174.1 -175.5 -177.9 10.8 84 I 345.8 0.005 -180.1 -174.1 -175.5 -177.9 10.8 85 I 346.7 0.005 -180.4 -174.3 -175.6 -178 9.0 86 I 345.9 0.005 -180.6 -174.4 -175.6 -178.1 9.6 87 I 345.9 0.004 -180.7 -174.7 -175.8 -178.2 9.9 88 I 347.9 0.004 -180.9 -175 -176 -178.5 10.2 89 I 344.6 0.003 -181 -175.2 -176.1 -178.7 12.4 90 I 344.6 0.003 -181.1 -175.3 -176.2 -178.8 12.4 91 I 343.9 0.002 -181.2 -175.6 -176.4 -179.1 9.6 92 I 342 0.002 -181.4 -175.7 -176.6 -179.2 12.4 93 I 343.6 0.002 -181.4 -175.8 -176.7 -179.3 9.5 94 I 342.4 0.001 -181.5 -175.8 -176.7 -179.4 9.8 95 I 342.3 0.001 -181.6 -175.8 -176.7 -179.4 10.3 96 I 341.3 0.001 -181.6 -176 -176.7 -179.5 11.0 97 I 342.2 0 -181.7 -176.2 -176.9 -179.7 12.4 98 I 339.5 0 -182 -176.6 -177.3 -180 9.8 99 I 339.7 0 -182.4 -176.8 -177.5 -180.2 9.8 100 I 337.5 0 -182.4 -177 -177.7 -180.4 12.4 101 I 336.5 0 -182.5 -177.1 -177.7 -180.5 12.4 102 I 337.7 0 -182.7 -177.2 -177.9 -180.7 9.4 103 I 335.8 0 -182.8 -177.4 -178 -180.9 10.6 104
EXP 7 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 135.6 1 -12.3 0.333 19.2 21 655.1 0.333 19 21.1 617.9 0.333 18.1 20.3 773.4 0.0 1 N 137.8 1 -23.3 0.333 17.9 18.8 224 0.333 17.9 19.2 174.6 0.333 17 18.1 224 0.0 2 N 145.6 1 -43.4 0.333 15.1 16.1 218.5 0.333 15.1 16.6 185.5 0.333 13.9 15.2 242.1 0.0 3 N 159.4 0.07 -73.5 0.333 11.9 12.9 204.9 0.333 11.9 13.5 181.3 0.333 10.4 11.7 227.6 0.0 4 S 174.4 0.067 -97.1 0.333 8.2 9.3 208.5 0.333 8 9.8 190.7 0.333 6 7.5 254.3 1.3 5
124
EXP 7 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 184.1 0.063 -114.4 0.333 3.9 5 225.6 0.333 3.5 5.5 204.2 0.333 0.9 2.4 278.2 0.0 6 N 187.1 0.064 -128.4 0.333 -1.1 0.1 197.9 0.333 -1.7 0.5 182.1 0.333 -4.8 -3.3 239.3 0.0 7 N 182.7 0.06 -173.7 0.333 -6.1 -5 204 0.333 -7.1 -4.9 193.6 0.333 -10.6 -9.3 254.6 0.0 8 N 193.7 0.057 -175.8 0.333 -10.7 -9.8 199.6 0.333 -12.1 -10 186.9 0.333 -16.1 -15 252.9 0.0 9 N 210 0.058 -175.5 0.333 -15.6 -14.8 207.1 0.333 -17.6 -15.4 202.7 0.333 -22.1 -21.2 282.2 0.0 10 N 206.4 0.057 -175.9 0.333 -20.5 -19.8 212.9 0.333 -23.1 -20.9 211.9 0.333 -28.2 -27.5 297.6 0.0 11 N 211 0.057 -176 0.333 -25.2 -24.6 208.7 0.333 -28.5 -26.3 212.6 0.333 -33.9 -33.5 293.5 0.0 12 N 214.6 0.056 -176.2 0.333 -29.9 -29.4 209.1 0.333 -33.9 -31.7 220.5 0.333 -39.5 -39.4 300.7 0.0 13 N 217.6 0.055 -176.5 0.333 -34.3 -33.9 200.4 0.333 -38.9 -36.9 215.2 0.333 -44.8 -45 294.7 0.0 14 S 211.1 0.056 -176.7 0.333 -38.6 -38.4 199.9 0.333 -43.7 -41.9 210.4 0.333 -49.7 -50.2 287.1 2.3 15 N 219.7 0.055 -176.9 0.333 -42.8 -42.7 197 0.333 -48.2 -46.5 205.2 0.333 -54.3 -55 279.4 0.0 16 N 219.2 0.055 -176.9 0.333 -46.7 -46.7 188.1 0.333 -52.3 -50.8 191.7 0.333 -58.5 -59.5 269 0.0 17 N 233.9 0.055 -176.7 0.333 -50.6 -50.8 189.3 0.333 -56.5 -55.2 200.8 0.333 -62.9 -64 278.6 0.0 18 N 229.5 0.054 -177.2 0.333 -54.4 -54.7 186.4 0.333 -60.9 -59.5 211.6 0.333 -67.2 -68.5 285.1 0.0 19 N 216 0.053 -177.6 0.333 -58.1 -58.4 181.7 0.333 -64.8 -63.7 203.2 0.333 -71.2 -72.6 274.7 0.0 20 S 220.2 0.054 -177.9 0.333 -61.5 -62 174.1 0.333 -68.4 -67.5 189.4 0.333 -74.8 -76.5 268.1 2.3 21 N 230.4 0.054 -177.8 0.333 -64.9 -65.5 177 0.333 -71.9 -71.1 186.9 0.333 -78.4 -80.3 269 0.0 22 S 232.6 0.054 -177.8 0.333 -68.1 -68.8 166.1 0.333 -75.3 -74.6 185.4 0.333 -81.7 -83.8 260.2 1.9 23
SW 224.1 0.054 -178 0.333 -71.3 -72.1 169.1 0.333 -78.7 -78.1 191.1 0.333 -85.1 -87.2 263.5 5.8 24 SW 214.8 0.054 -178.6 0.333 -74.2 -75.2 158.5 0.333 -81.7 -81.3 179.1 0.333 -88.1 -90.4 253.9 5.2 25 SW 211.4 0.054 -179 0.333 -77 -78.2 151.8 0.333 -84.5 -84.3 166.6 0.333 -90.9 -93.4 245.3 4.8 26 SW 209.2 0.054 -179.3 0.333 -79.8 -81.1 156.3 0.333 -87.4 -87.2 168.3 0.333 -93.9 -96.4 254.4 5.7 27 SW 206.5 0.054 -179.6 0.333 -82.3 -83.8 143.4 0.333 -89.9 -89.9 158.2 0.333 -96.5 -99.2 247.2 3.6 28 SW 220.3 0.055 -179.6 0.333 -84.7 -86.3 136.5 0.333 -92.4 -92.5 150.9 0.333 -99 -101.8 241.7 5.2 29 SW 221.6 0.058 -179.6 0.333 -87 -88.7 131.1 0.333 -94.7 -94.9 144.9 0.333 -101.4 -104.4 243.2 6.1 30 SW 212.4 0.058 -179.8 0.333 -89.1 -91 126.3 0.333 -96.9 -97.2 141 0.333 -103.7 -106.8 237.5 4.4 31 SW 205.4 0.058 -180.2 0.333 -91.3 -93.2 127.8 0.333 -99.1 -99.4 137.4 0.333 -105.9 -109.1 239.3 6.9 32 SW 222.2 0.062 -180 0.333 -93.3 -95.3 121.5 0.333 -101.1 -101.5 130.2 0.333 -108 -111.3 238.2 3.3 33 SW 225.1 0.061 -180.3 0.333 -95.2 -97.4 116.3 0.333 -103.1 -103.6 132.2 0.333 -110 -113.4 231.8 5.0 34 SW 212 0.062 -180.5 0.333 -97 -99.3 111.6 0.333 -105 -105.6 121.8 0.333 -112 -115.5 238.1 3.9 35 SW 216.8 0.064 -180.7 0.333 -98.8 -101.2 111.8 0.333 -106.8 -107.5 128.1 0.333 -113.8 -117.4 228.2 4.3 36 SW 215.7 0.063 -180.9 0.333 -100.6 -103 112.3 0.333 -108.6 -109.4 122.4 0.333 -115.5 -119.2 225.3 3.5 37 SW 202.2 0.063 -181 0.333 -102.2 -104.8 101.1 0.333 -110.3 -111.1 117.2 0.333 -117.1 -120.9 223.3 7.3 38 SW 203.1 0.067 -180.9 0.333 -103.9 -106.5 108.1 0.333 -111.9 -112.8 119.2 0.333 -118.8 -122.6 230.6 3.5 39 SW 208.7 0.073 -180.6 0.333 -105.4 -108.1 101.3 0.333 -113.5 -114.4 113.5 0.333 -120.4 -124.2 226.4 5.2 40 SW 216.2 0.075 -180.8 0.333 -107 -109.8 102.6 0.333 -115 -116.1 115.8 0.333 -121.9 -125.8 226 3.3 41 SW 218 0.082 -180.6 0.333 -108.5 -111.4 104.2 0.333 -116.6 -117.7 120.7 0.333 -123.4 -127.3 231.7 2.8 42 SW 257 0.086 -180.3 0.333 -110.1 -113 106 0.333 -118.2 -119.3 125.5 0.333 -124.9 -128.9 241.7 2.5 43
125
EXP 7 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 259.1 0.084 -180.5 0.333 -111.5 -114.5 101.8 0.333 -119.6 -120.8 111.3 0.333 -126.3 -130.4 238.3 4.6 44 SW 251.4 0.088 -180.1 0.333 -113 -116 101.4 0.333 -121.1 -122.3 119.4 0.333 -127.8 -131.9 243 4.1 45 SW 249.7 0.086 -180.3 0.333 -114.4 -117.5 101.7 0.333 -122.5 -123.8 123.3 0.333 -129.1 -133.3 240.7 3.4 46 SW 242.8 0.086 -180.3 0.333 -115.8 -118.9 102.1 0.333 -124 -125.3 133.2 0.333 -130.4 -134.6 238.5 3.4 47 SW 244.4 0.088 -180 0.333 -117.2 -120.4 105.5 0.333 -125.4 -126.8 129.8 0.333 -131.8 -136 246.2 4.1 48 SW 242 0.087 -180.3 0.333 -118.6 -121.9 107.9 0.333 -126.8 -128.3 130.2 0.333 -133.1 -137.3 247.5 4.0 49 SW 232.5 0.09 -180.1 0.333 -119.9 -123.3 102 0.333 -128 -129.5 112.6 0.333 -134.3 -138.5 241.7 2.8 50 SW 227.4 0.087 -180.4 0.333 -121.3 -124.7 108.1 0.333 -129.3 -130.9 125.9 0.333 -135.5 -139.8 249.9 3.0 51 SW 228 0.09 -180.1 0.333 -122.6 -126.1 107.2 0.333 -130.5 -132.2 127.6 0.333 -136.6 -141 247.7 3.2 52 SW 222.5 0.088 -180.3 0.333 -123.8 -127.4 101.2 0.333 -131.8 -133.5 129.3 0.333 -137.7 -142.1 239.8 5.9 53 SW 216.4 0.088 -180.5 0.333 -125.1 -128.7 104.7 0.333 -132.9 -134.7 120.8 0.333 -138.7 -143.1 240 3.7 54 SW 212.1 0.088 -180.5 0.333 -126.2 -130 99.2 0.333 -134 -135.9 118.8 0.333 -139.8 -144.2 244.7 3.8 55 SW 209.6 0.086 -180.8 0.333 -127.4 -131.2 103.1 0.333 -135 -137 115.1 0.333 -140.8 -145.3 248.1 6.3 56 SW 205.3 0.088 -180.6 0.333 -128.5 -132.4 100.6 0.333 -136.1 -138.1 116.7 0.333 -141.8 -146.3 251.1 5.5 57 SW 196.7 0.086 -181.1 0.333 -129.9 -133.8 128.8 0.333 -137.1 -139.1 109.8 0.333 -142.7 -147.3 246.3 2.9 58 SW 205.1 0.084 -180.9 0.333 -130.7 -134.8 78.4 0.333 -138 -140.1 104 0.333 -143.8 -148.3 269.6 3.3 59 SW 205.2 0.086 -180.7 0.333 -131.6 -135.7 86.2 0.333 -139.1 -141.2 108.5 0.333 -145.5 -149.9 361 3.0 60 SW 205.7 0.027 -181.1 0.417 -133.1 -136.8 86.1 0.292 -146 -145.2 337.9 0.292 -164.5 -166.1 2941 6.2 61 SW 206.9 0.008 -180.6 0.417 -136.7 -137.8 5.8 0.292 -164.3 -161.1 2648.8 0.292 -172.2 -174.1 3480.1 8.9 62 SW 204.6 0.078 -180.8 -139 -169.9 -175.4 4.3 63 SW 199.2 0.081 -180.7 -140.9 -173.2 -175.8 4.1 64 SW 200.6 0.076 -180.8 -143.6 -174.7 -176.1 3.5 65 SW 208 0.076 -180.9 -147 -175.3 -176.2 2.6 66 SW 204.5 0.077 -180.7 -151.2 -175.8 -176.4 6.9 67 SW 205.9 0.075 -180.8 -156.3 -176.1 -176.5 5.0 68 SW 204.2 0.076 -180.9 -163 -176.3 -176.5 2.6 69 SW 193.7 0.078 -180.8 -171.3 -176.6 -176.7 4.0 70 SW 200.4 0.073 -181.4 -174.9 -176.9 -176.9 3.8 71 SW 192.1 0.078 -181 -175.8 -177.1 -177.1 3.5 72 SW 185.8 0.075 -181.3 -176.4 -177.4 -177.3 3.7 73 SW 189.7 0.074 -181.5 -176.5 -177.3 -177.3 5.6 74 SW 173.9 0.078 -181.1 -176.7 -177.5 -177.4 5.0 75 SW 178.6 0.072 -181.9 -176.8 -177.6 -177.6 3.4 76 SW 172 0.077 -181.6 -177 -177.7 -177.8 4.9 77 SW 162.6 0.076 -182 -177.4 -178.1 -178.1 4.0 78 SW 170.4 0.073 -182.6 -177.6 -178.3 -178.3 4.3 79 SW 154.2 0.08 -182.4 -178.1 -178.8 -178.8 2.8 80 SW 164.4 0.073 -183.4 -178.5 -179.1 -179.2 4.4 81
126
EXP 7 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 157.3 0.077 -183.3 -178.8 -179.4 -179.5 4.3 82 SW 147.9 0.078 -183.7 -179.3 -179.9 -179.9 4.9 83 SW 156.8 0.074 -184.3 -179.6 -180.2 -180.2 2.7 84 SW 145.8 0.079 -183.9 -179.8 -180.4 -180.6 5.4 85 SW 154.3 0.072 -184.6 -180 -180.6 -180.7 6.4 86 SW 148.9 0.076 -184.5 -180.1 -180.8 -180.9 6.1 87 SW 146.4 0.074 -184.7 -180.3 -181 -181.2 4.8 88 SW 141.9 0.076 -185 -180.4 -181.1 -181.3 3.8 89 SW 139.9 0.075 -184.9 -180.6 -181.3 -181.5 2.2 90 SW 148.8 0.071 -185.2 -180.7 -181.3 -181.6 5.3 91 SW 134.5 0.077 -185.1 -180.8 -181.4 -181.7 2.4 92 SW 146.2 0.068 -185.3 -181 -181.6 -181.9 5.3 93 SW 137.3 0.074 -185.3 -181 -181.6 -181.9 5.0 94 SW 137.3 0.071 -185.5 -181.2 -181.8 -182.1 4.7 95 SW 138.6 0.071 -185.6 -181.4 -182 -182.3 4.3 96 SW 133.8 0.072 -185.9 -181.7 -182.3 -182.7 3.3 97 SW 143.4 0.068 -186.5 -182.2 -182.8 -183.1 4.2 98 SW 131.7 0.073 -186.8 -182.5 -183.2 -183.5 3.0 99 SW 133.5 0.07 -187.3 -183 -183.7 -184.1 2.3 100 SW 137.2 0.069 -187.8 -183.5 -184.2 -184.6 2.8 101 SW 131.2 0.071 -187.9 -183.9 -184.7 -185 6.2 102 SW 140.1 0.066 -188.6 -184.3 -184.9 -185.3 2.9 103 SW 125.7 0.072 -188.5 -184.6 -185.3 -185.7 3.7 104 SW 130.7 0.068 -189.1 -184.8 -185.6 -186 2.5 105 SW 128.2 0.07 -189.2 -185.1 -185.9 -186.3 2.4 106 SW 124.3 0.07 -189.5 -185.4 -186.1 -186.6 2.7 107 SW 134.4 0.065 -189.6 -185.6 -186.4 -186.9 2.4 108 SW 125.8 0.07 -189.8 -185.7 -186.6 -187.1 3.1 109 SW 123.7 0.068 -190 -185.9 -186.7 -187.2 2.7 110 SW 126 0.067 -189.9 -185.9 -186.7 -187.3 4.6 111 SW 124.6 0.067 -189.9 -185.8 -186.7 -187.2 3.2 112 SW 131 0.064 -190.1 -186.1 -187 -187.6 2.9 113 SW 134.8 0.063 -190.4 -186.3 -187.2 -187.9 3.6 114 SW 121.2 0.068 -190.5 -186.5 -187.4 -188.1 4.5 115 SW 122.2 0.066 -190.8 -186.8 -187.7 -188.3 5.1 116 SW 117.2 0.068 -190.9 -187 -187.9 -188.6 5.2 117 SW 123.8 0.064 -190.9 -187 -188 -188.7 7.4 118 SW 123.7 0.064 -191 -187.2 -188.2 -188.9 4.8 119
127
EXP 7 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 121.4 0.064 -191.4 -187.5 -188.5 -189.2 3.2 120 SW 125.1 0.063 -191.6 -187.8 -188.8 -189.6 4.8 121 SW 121.6 0.064 -191.7 -187.8 -188.8 -189.7 6.1 122 SW 115.3 0.065 -191.8 -188 -189 -189.9 3.6 123 SW 124.5 0.061 -192 -188.2 -189.1 -190 3.4 124 SW 114.4 0.066 -192.1 -188.3 -189.3 -190.3 3.9 125 SW 120 0.061 -192.3 -188.5 -189.6 -190.4 4.2 126 SW 124.4 0.06 -192.2 -188.5 -189.5 -190.5 4.7 127 SW 117.3 0.063 -192.3 -188.5 -189.6 -190.6 4.0 128 SW 119.7 0.06 -192.7 -189 -190.1 -191.1 3.7 129 SW 115.5 0.062 -192.8 -189.2 -190.2 -191.3 4.3 130 SW 118.5 0.06 -192.8 -189 -190.1 -191.2 3.1 131 SW 116.1 0.061 -192.4 -188.8 -189.9 -191 3.2 132 SW 121 0.059 -192.2 -188.5 -189.6 -190.8 4.2 133 SW 117.9 0.06 -192.1 -188.3 -189.5 -190.7 3.8 134 SW 113.6 0.06 -192.1 -188.3 -189.5 -190.7 4.6 135 SW 118.1 0.059 -192.1 -188.3 -189.5 -190.6 8.9 136 SW 114 0.06 -192 -188.2 -189.4 -190.6 2.7 137 SW 118.6 0.058 -191.8 -188.1 -189.3 -190.5 5.5 138 SW 118.3 0.058 -191.8 -188 -189.2 -190.5 6.6 139 SW 112.8 0.06 -191.8 -188 -189.2 -190.5 5.0 140 SW 114 0.059 -191.9 -188 -189.3 -190.6 3.5 141 SW 113.1 0.059 -192.1 -188.3 -189.6 -190.9 5.8 142 SW 120.5 0.055 -192.7 -188.8 -190.1 -191.3 5.3 143 SW 106.8 0.061 -193 -189.4 -190.6 -192 6.2 144 SW 116.2 0.056 -193.8 -190.1 -191.3 -192.7 5.4 145
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 71.9 1 3.5 0.333 21.4 22.7 780.7 0.333 21.2 22.9 663.1 0.333 20.1 21.8 1060 0.0 1 N 73.6 1 0.9 0.333 21.4 21.9 169.2 0.333 21.3 22.2 89.3 0.333 20.5 21.2 139.7 0.0 2 N 75.3 1 -1.3 0.333 20.6 21.1 237.8 0.333 20.5 21.5 157.6 0.333 19.7 20.4 233.8 0.0 3 N 76 1 -3.9 0.333 19.7 20.2 238.7 0.333 19.8 20.7 162.9 0.333 18.9 19.6 244.4 0.0 4 N 76.4 1 -6.4 0.333 18.8 19.3 250.9 0.333 18.9 19.9 166.8 0.333 18 18.7 251.6 0.0 5 N 76.8 1 -8.9 0.333 17.9 18.3 237.5 0.333 18 19 154.6 0.333 17.1 17.8 244.7 0.0 6 N 77.8 1 -12.4 0.333 16.8 17.2 237.1 0.333 17 17.9 162.3 0.333 16 16.7 244.6 0.0 7
128
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t N 78.3 1 -16.9 0.333 15.7 16 224 0.333 15.9 16.9 152.6 0.333 14.8 15.5 240.1 0.0 8 N 79.3 1 -22.8 0.333 14.4 14.7 196.1 0.333 14.7 15.6 136 0.333 13.5 14.2 206.3 0.0 9 N 80.4 1 -34.3 0.333 12.9 13.3 162.5 0.333 13.2 14.3 117.7 0.333 11.9 12.6 178.5 0.0 10 N 82.1 1 -53.3 0.333 11.3 11.6 145.6 0.333 11.5 12.6 110.2 0.333 9.8 10.6 186 0.0 11 N 84.5 1 -72.2 0.333 9.5 9.8 136.1 0.333 9.5 10.8 103.9 0.333 7.3 8.1 192.4 0.0 12 N 87.3 1 -89.7 0.333 7.6 7.9 130.1 0.333 7.2 8.7 105.2 0.333 4.2 5.1 215.1 0.0 13 N 90.3 1 -101.4 0.333 5.4 5.8 132.8 0.333 4.6 6.3 110.4 0.333 0.7 1.5 241 0.0 14 N 94.7 1 -110.6 0.333 3.2 3.5 132.1 0.333 1.7 3.6 114.9 0.333 -3.1 -2.3 248.9 0.0 15 N 99 0.346 -118.4 0.333 0.7 1.1 137.6 0.333 -1.5 0.6 129.2 0.333 -6.9 -6.3 256.6 0.1 16 N 97.6 0.193 -123.8 0.333 -1.6 -1.2 128.7 0.333 -4.5 -2.3 122.2 0.333 -10.6 -10.3 256.3 0.0 17 N 97.8 0.131 -127.8 0.333 -3.9 -3.5 96.8 0.333 -7.5 -5.2 92.9 0.333 -14.2 -14.1 199.3 0.0 18
SW 101.1 0.098 -165.5 0.333 -6.2 -5.8 92.6 0.333 -10.5 -8.2 93.1 0.333 -17.8 -17.9 196.6 3.2 19 SW 103.6 0.078 -169.8 0.333 -8.5 -8.1 93 0.333 -13.4 -11 90.7 0.333 -21.2 -21.6 198 3.7 20 SW 107.1 0.064 -170.1 0.333 -10.9 -10.4 92.2 0.333 -16.4 -14 94.1 0.333 -24.7 -25.2 204 2.9 21 N 112.2 0.054 -170.2 0.333 -13.2 -12.6 90.4 0.333 -19.4 -16.9 94.9 0.333 -28.3 -29 218.1 0.0 22
SW 120.1 0.046 -170.2 0.333 -15.5 -14.9 90.3 0.333 -22.4 -19.8 97.2 0.333 -31.9 -32.8 221.7 3.3 23 N 121.8 0.042 -170 0.333 -17.8 -17.2 89.8 0.333 -25.4 -22.8 97.9 0.333 -35.4 -36.4 226.5 0.0 24
SW 127.6 0.036 -170.2 0.333 -20.1 -19.4 87.6 0.333 -28.3 -25.6 95.1 0.333 -38.6 -39.9 223.6 2.1 25 SW 124.4 0.036 -169.9 0.333 -22.4 -21.7 88.4 0.333 -31.1 -28.5 96.2 0.333 -41.9 -43.4 230.2 2.8 26 SW 126.3 0.031 -170.3 0.333 -24.7 -24 87.2 0.333 -33.9 -31.3 96.1 0.333 -44.9 -46.6 223.8 2.6 27 SW 145.8 0.027 -170.1 0.333 -27.1 -26.3 88.3 0.333 -36.7 -34.1 99.2 0.333 -47.9 -49.7 225.9 1.9 28 SW 128.9 0.03 -169.9 0.333 -29.4 -28.6 86.7 0.333 -39.5 -36.8 96.9 0.333 -51.2 -53.1 245.7 3.3 29 SW 143 0.022 -170.7 0.333 -31.5 -30.7 81.1 0.333 -42 -39.4 90.9 0.333 -53.8 -56 227.1 8.1 30 SW 171.6 0.024 -170.1 0.333 -33.9 -33.1 91.5 0.333 -44.5 -42 92.3 0.333 -56.4 -58.8 223.2 6.4 31 SW 126 0.026 -169.8 0.333 -35.9 -35.2 76.8 0.333 -47.1 -44.5 91.9 0.333 -59.3 -61.7 241.4 5.6 32 SW 146.4 0.019 -171.1 0.333 -38 -37.3 74.6 0.333 -49.4 -47 92.5 0.333 -61.5 -64.2 216.3 8.0 33 SW 180.6 0.021 -170.2 0.333 -40.4 -39.7 94.3 0.333 -51.8 -49.4 92.3 0.333 -64 -66.7 231.9 3.7 34 SW 137 0.022 -169.6 0.333 -42.5 -41.8 77.9 0.333 -54.3 -51.8 90.2 0.333 -67 -69.7 259.9 6.4 35 SW 149.3 0.017 -171 0.333 -44.6 -43.9 79.5 0.333 -56.8 -54.4 102.1 0.333 -69.4 -72.3 239.3 6.8 36 SW 186.8 0.017 -170.8 0.333 -46.9 -46.2 89.4 0.333 -59 -56.7 90.1 0.333 -71.5 -74.6 232.9 6.7 37 SW 166.1 0.019 -169.6 0.333 -49.1 -48.5 86.9 0.333 -61.3 -59 91.2 0.333 -74.4 -77.3 268.1 3.3 38 SW 155 0.017 -170.7 0.333 -50.9 -50.5 72.7 0.333 -63.5 -61.3 88.6 0.333 -76.7 -79.9 256.2 1.6 39 SW 181.6 0.015 -171.4 0.333 -53 -52.6 81.7 0.333 -65.6 -63.5 90.4 0.333 -78.6 -82 232.6 5.9 40 SW 184.7 0.017 -169.8 0.333 -55 -54.6 76.7 0.333 -67.8 -65.6 85.5 0.333 -81.1 -84.5 272 4.2 41 SW 146 0.018 -170.1 0.333 -56.9 -56.6 72 0.333 -70.1 -68 97.7 0.333 -83.6 -87 270.6 6.6 42 SW 165.3 0.013 -171.8 0.333 -58.8 -58.5 72.4 0.333 -72.1 -70.1 89.1 0.333 -85.3 -88.9 240.9 8.3 43 SW 201.3 0.015 -170.4 0.333 -60.9 -60.6 82.5 0.333 -74.2 -72.2 90.6 0.333 -87.4 -91.1 266 4.6 44 SW 157.5 0.017 -169.7 0.333 -63 -62.7 84.2 0.333 -76.4 -74.3 92.9 0.333 -90 -93.6 297.2 5.4 45
129
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t SW 172.4 0.013 -171.6 0.333 -64.7 -64.7 71.9 0.333 -78.2 -76.3 83.7 0.333 -91.8 -95.6 259.8 7.8 46 SW 196.9 0.013 -171.2 0.333 -66.8 -66.7 86.1 0.333 -80.1 -78.4 95.8 0.333 -93.2 -97.2 238.7 5.4 47 SW 178.1 0.014 -169.5 0.333 -68.9 -68.9 87.1 0.333 -82.4 -80.6 111.6 0.333 -95.5 -99.3 287.1 3.1 48 SW 159.2 0.014 -170.4 0.333 -70.7 -70.8 75.8 0.333 -84.3 -82.6 91.2 0.333 -97.4 -101.3 273.3 3.1 49 SW 174.6 0.011 -172.4 0.333 -72.5 -72.7 76 0.333 -85.8 -84.4 80.9 0.333 -98.6 -102.7 233.5 10.4 50 SW 194.3 0.012 -170.2 0.333 -74.5 -74.7 88 0.333 -87.8 -86.3 98.6 0.333 -100.6 -104.6 288.8 3.7 51 SW 152.7 0.015 -169.6 0.333 -76.3 -76.7 80 0.333 -89.8 -88.3 104.4 0.333 -102.6 -106.7 294.6 4.8 52 SW 173.1 0.011 -171.9 0.333 -78.1 -78.5 75.6 0.333 -91.4 -90.1 88.7 0.333 -104.1 -108.3 266.7 5.6 53 SW 196.1 0.011 -171.3 0.333 -79.9 -80.4 86.5 0.333 -93 -91.8 81 0.333 -105.5 -109.8 265.4 6.7 54 SW 173.8 0.013 -169.6 0.333 -81.9 -82.5 94.9 0.333 -95 -93.8 107.6 0.333 -107.7 -111.8 320.2 2.3 55 SW 158.3 0.013 -170.5 0.333 -83.6 -84.3 81 0.333 -96.7 -95.6 93.5 0.333 -109.3 -113.6 294 3.7 56 SW 173.4 0.01 -172.4 0.333 -85.2 -86.1 77.1 0.333 -98.1 -97.2 82.6 0.333 -110.3 -114.8 245.8 8.9 57 SW 189.8 0.011 -170.6 0.333 -86.9 -87.8 81.6 0.333 -99.7 -98.8 84.6 0.333 -111.9 -116.3 300.7 4.9 58 SW 179.6 0.012 -169.7 0.333 -88.5 -89.5 77 0.333 -101.6 -100.6 109.2 0.333 -114 -118.3 339.7 5.7 59 SW 178.9 0.012 -170.7 0.333 -89.9 -91.1 65.3 0.333 -103 -102.2 84.1 0.333 -115.3 -119.8 291.4 3.2 60 SW 176.2 0.009 -172.5 0.333 -91.4 -92.6 70.8 0.333 -104.3 -103.7 82.9 0.333 -116.1 -120.8 245.2 7.1 61 SW 190.4 0.01 -170.8 0.333 -93 -94.2 76.6 0.333 -105.7 -105.1 76.3 0.333 -117.7 -122.2 317.7 5.0 62 SW 177.2 0.012 -169.8 0.333 -94.6 -95.9 80.7 0.333 -107.4 -106.8 108.5 0.333 -119.5 -123.9 351.7 7.0 63 SW 192.9 0.013 -170.1 0.333 -96 -97.4 70.5 0.333 -108.8 -108.3 83.8 0.333 -120.8 -125.4 309.6 3.6 64 SW 176.1 0.01 -172.4 0.333 -97.4 -98.9 74 0.333 -110 -109.6 77.6 0.333 -121.6 -126.4 261.3 7.3 65 SW 174.8 0.009 -171.8 0.333 -98.8 -100.4 76.9 0.333 -111.1 -110.9 71.5 0.333 -122.6 -127.4 287.6 11.1 66 SW 150.1 0.012 -170.4 0.333 -100 -101.8 60.7 0.333 -112.5 -112.2 74.3 0.333 -124.3 -128.9 370.4 7.2 67 SW 223.2 0.014 -169.7 0.333 -101.2 -103 59.9 0.333 -113.9 -113.6 90.1 0.333 -125.9 -130.5 367.5 7.3 68 SW 209.3 0.013 -170.8 0.333 -102.5 -104.3 58.7 0.333 -115.1 -114.9 77.1 0.333 -126.9 -131.7 313.7 5.4 69 SW 191.3 0.009 -172.5 0.333 -103.8 -105.6 67.5 0.333 -116.2 -116.1 76.3 0.333 -127.5 -132.5 275 8.3 70 SW 164.4 0.009 -171.4 0.333 -105 -106.9 66.9 0.333 -117.3 -117.3 68.9 0.333 -128.6 -133.5 325.6 10.7 71 SW 196.4 0.012 -170.2 0.333 -106.1 -108.1 56.6 0.333 -118.7 -118.6 98.6 0.333 -130.3 -135 409 8.4 72 SW 253.2 0.012 -169.7 0.333 -107.2 -109.3 54 0.333 -120.1 -120 100.1 0.333 -131.6 -136.4 406.5 8.8 73 SW 183.6 0.014 -169.8 0.333 -108.5 -110.6 66.4 0.333 -121.2 -121.3 83.2 0.333 -132.6 -137.6 345.5 4.7 74 SW 181.3 0.01 -172.6 0.333 -109.8 -111.9 73.1 0.333 -122.2 -122.4 79.1 0.333 -133 -138.1 259 3.5 75 SW 177.7 0.007 -172.8 0.333 -111.1 -113.3 79.6 0.333 -123 -123.4 73.9 0.333 -133.2 -138.4 244.5 4.2 76 SW 153.1 0.008 -170.9 0.333 -112.3 -114.6 75.2 0.333 -124.1 -124.5 84.7 0.333 -134.6 -139.4 383.3 9.0 77 SW 198 0.01 -169.9 0.333 -113.2 -115.6 45.2 0.333 -125.3 -125.6 94.7 0.333 -136 -140.8 433.3 6.2 78 SW 214.2 0.011 -169.8 0.333 -114.3 -116.7 60.7 0.333 -126.3 -126.7 76.8 0.333 -136.9 -141.9 382.8 6.9 79 SW 165.1 0.011 -171.2 0.333 -115.4 -117.9 70.2 0.333 -127.2 -127.7 76.7 0.333 -137.6 -142.6 313.4 6.1 80 SW 184.3 0.007 -173.6 0.333 -116.6 -119.1 70.8 0.333 -128.1 -128.8 88.5 0.333 -137.8 -143 261.9 4.8 81 SW 164 0.007 -172.1 0.333 -117.8 -120.5 88.6 0.333 -129.7 -130 94.4 0.333 -140.7 -145.3 672.1 9.8 82
I 156.4 0.008 -170.5 0.417 -120.1 -121.8 63.6 0.292 -140.6 -137.4 963.7 0.292 -157.1 -158.4 3147.7 9.6 83
130
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 202.8 0.009 -170 0.417 -123.6 -123.1 30.3 0.292 -154.1 -151 3313.8 0.292 -160.9 -163.6 3123 10.8 84 I 187.1 0.009 -170.2 0.417 -126.5 -124.8 33.7 0.292 -158.4 -157.6 3669.5 0.292 -160.6 -164.9 930 6.1 85 I 152 0.009 -171.9 0.417 -129.3 -127 67.9 0.292 -159.1 -159.4 2415.9 0.292 -161.6 -165.9 811.8 5.7 86 I 182.2 0.007 -173.5 0.417 -132.1 -129.8 119.3 0.292 -159.9 -160.6 2192.2 0.292 -163.8 -167.9 1717.4 4.5 87 I 138.2 0.007 -172.7 0.417 -135 -132.7 112.7 0.292 -162.1 -163.3 3950.2 0.292 -164.2 -168.5 1242.4 12.4 88 I 199 0.008 -171.6 -135.9 -165.4 -168.5 12.0 89 I 201.4 0.008 -171.2 -140.4 -166 -168.2 12.1 90 I 193.7 0.007 -171.1 -145.4 -166.3 -167.9 10.1 91 I 187 0.007 -171.2 -150.7 -166.5 -167.5 9.3 92 I 188.2 0.007 -171.5 -155.6 -166.8 -167.4 10.2 93 I 197.9 0.006 -171.9 -161.1 -166.9 -167.5 9.2 94 I 205.9 0.006 -172.2 -164.9 -167.1 -167.8 12.4 95 I 212.9 0.006 -172.2 -165.8 -167.4 -168.1 8.7 96 I 217.8 0.006 -172.6 -166.2 -167.6 -168.4 12.3 97 I 223.4 0.005 -172.8 -166.4 -168 -168.7 11.8 98 I 232.2 0.005 -173 -166.6 -168.3 -169 12.3 99 I 243.4 0.005 -173.3 -166.7 -168.6 -169.3 11.6 100 I 248.9 0.005 -173.5 -166.9 -169 -169.7 10.9 101 I 252.7 0.005 -173.9 -167.1 -169.3 -170 12.2 102 I 257 0.004 -174.1 -167.4 -169.7 -170.4 12.1 103 I 258.5 0.004 -174.4 -167.7 -170 -170.7 12.4 104 I 261.8 0.004 -174.7 -168 -170.2 -171 12.3 105 I 266.4 0.004 -175 -168.3 -170.5 -171.2 12.4 106 I 264.9 0.004 -175.2 -168.5 -170.8 -171.5 12.4 107 I 267 0.003 -175.3 -168.7 -171 -171.6 12.4 108 I 263.7 0.003 -175.4 -168.9 -171.2 -171.8 12.1 109 I 261.4 0.003 -175.6 -169.1 -171.3 -172 10.7 110 I 261.1 0.003 -175.8 -169.3 -171.5 -172.1 12.4 111 I 259.7 0.003 -176.1 -169.6 -171.7 -172.3 12.4 112 I 259.7 0.003 -176.3 -169.8 -171.8 -172.4 12.4 113 I 262.7 0.002 -176.4 -170 -172 -172.6 12.4 114 I 263.2 0.002 -176.6 -170.2 -172.2 -172.8 12.4 115 I 264.7 0.002 -176.7 -170.3 -172.4 -173 12.4 116 I 260.8 0.002 -176.7 -170.5 -172.5 -173.2 12.3 117 I 257.5 0.002 -176.8 -170.7 -172.6 -173.3 11.9 118 I 257.5 0.002 -176.8 -170.8 -172.6 -173.4 12.3 119 I 260.5 0.001 -176.9 -170.8 -172.7 -173.4 11.5 120 I 262.6 0.001 -177 -170.9 -172.8 -173.5 11.8 121
131
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t I 263.8 0.001 -177.1 -171 -172.8 -173.6 11.3 122 I 264.8 0.001 -177.3 -171.1 -173 -173.7 10.2 123
1φ 263.2 0.001 -177.5 -171.3 -173.1 -173.9 12.4 124 1φ 261.5 0 -177.7 -171.4 -173.2 -174.1 12.4 125 1φ 261.1 0 -177.7 -171.6 -173.4 -174.3 12.3 126 1φ 260.7 0 -177.8 -171.8 -173.6 -174.4 12.3 127 1φ 262.8 0 -177.9 -172 -173.7 -174.6 12.4 128 1φ 261.3 0 -178 -172.3 -174 -174.8 12.4 129 1φ 262.7 0 -178.1 -172.6 -174.2 -175.1 12.1 130 1φ 260.1 0 -178.3 -172.8 -174.4 -175.3 11.0 131 1φ 259.9 0 -178.5 -173.1 -174.5 -175.5 12.4 132 1φ 259.8 0 -178.7 -173.3 -174.7 -175.7 12.4 133 1φ 257.7 0 -179.2 -173.5 -174.9 -175.9 12.4 134 1φ 257 0 -179.6 -173.9 -175.1 -176.1 12.4 135 1φ 255.2 0 -179.6 -174.2 -175.2 -176.2 12.4 136 1φ 254.2 0 -179.8 -174.6 -175.4 -176.4 11.7 137 1φ 253 0 -179.9 -174.7 -175.6 -176.5 12.4 138 1φ 251.8 0 -180.1 -174.9 -175.7 -176.6 12.4 139 1φ 251.2 0 -180.2 -175.1 -175.8 -176.8 12.4 140 1φ 249.3 0 -180.3 -175.2 -176 -177 12.0 141 1φ 249.6 0 -180.5 -175.4 -176.1 -177.1 12.4 142 1φ 248.6 0 -180.6 -175.4 -176.2 -177.2 12.4 143 1φ 248.5 0 -180.6 -175.5 -176.3 -177.3 11.9 144 1φ 247.2 0 -180.6 -175.5 -176.4 -177.4 12.4 145 1φ 248 0 -180.9 -175.6 -176.4 -177.4 12.4 146 1φ 248.4 0 -180.8 -175.6 -176.5 -177.5 12.4 147 1φ 245.4 0 -180.9 -175.7 -176.5 -177.6 12.4 148 1φ 245.8 0 -181.1 -175.8 -176.6 -177.7 12.4 149 1φ 246.3 0 -181.1 -176 -176.7 -177.8 12.4 150 1φ 245.8 0 -181.2 -176.2 -176.9 -177.9 12.4 151 1φ 244.8 0 -181.6 -176.3 -176.9 -178 12.4 152 1φ 243.3 0 -181.6 -176.4 -177.1 -178.2 12.4 153 1φ 241.4 0 -181.5 -176.5 -177.2 -178.2 12.4 154 1φ 243 0 -181.7 -176.6 -177.2 -178.4 12.4 155 1φ 242.5 0 -181.7 -176.6 -177.2 -178.5 12.4 156 1φ 242.7 0 -181.8 -176.7 -177.3 -178.5 12.4 157
132
EXP 8 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t 1φ 241 0 -182 -176.7 -177.4 -178.6 12.4 158 1φ 239.6 0 -182 -176.8 -177.5 -178.7 12.4 159 1φ 237.8 0 -182 -176.9 -177.6 -178.8 12.4 160 1φ 237.8 0 -182 -177 -177.7 -178.9 12.4 161 1φ 236 0 -182.2 -177.1 -177.8 -178.9 12.4 162
EXP 9 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 24.9 1 19.6 0.33 23.6 24.3 766.5 0.33 23.7 24.4 626.7 0.33 23 24.4 666 0.0 1 0.107 N 44.9 1 17.6 0.33 23.6 24.1 96.5 0.33 23.8 24.3 66.9 0.33 23.1 24.3 0.9 0.0 2 0.294 N 53.5 1 15.1 0.33 23.3 23.8 198.4 0.33 23.5 24 132 0.33 22.8 24 203.1 0.0 3 0.324 N 55 1 13.1 0.33 23 23.5 214.9 0.33 23.1 23.7 145.7 0.33 22.3 23.6 257.7 0.0 4 0.337 N 55.5 1 11.7 0.33 22.4 23 299.9 0.33 22.6 23.2 319.5 0.33 22 23.2 211.7 0.0 5 0.337 N 55 1 10.4 0.33 22.1 22.6 222.5 0.33 22.2 22.8 155.9 0.33 21.5 22.7 253.3 0.0 6 0.344 N 56 1 8.8 0.33 21.6 22 296.4 0.33 21.9 22.5 111 0.33 21.3 22.4 130.5 0.0 7 0.348 N 56.3 1 7.6 0.33 21 21.5 247.4 0.33 21.2 21.9 244.3 0.33 20.4 21.7 327.6 0.0 8 0.339 N 56.3 1 5.8 0.33 20.5 20.9 262.9 0.33 20.8 21.4 168.3 0.33 20.1 21.3 179.8 0.0 9 0.351 N 57 1 4.4 0.33 19.7 20.1 308.8 0.33 20 20.7 260.7 0.33 19.4 20.6 270.9 0.0 10 0.344 N 57.3 0.643 2.5 0.33 19.2 19.5 271.5 0.33 19.6 20.2 106.7 0.33 18.8 20 222.8 0.0 11 0.34 N 57.8 0.379 0.9 0.33 18.4 18.7 298.8 0.33 18.7 19.4 258.4 0.33 18 19.2 293.7 0.0 12 0.336 N 57.6 0.269 -0.9 0.33 17.6 17.9 295 0.33 17.9 18.7 205 0.33 17.2 18.3 290.5 0.0 13 0.344 N 58.1 0.204 -2.9 0.33 17.1 17.2 210.3 0.33 17.5 18.1 135.8 0.33 16.8 17.8 169.1 0.0 14 0.346 N 58.8 0.162 -4.8 0.33 16.1 16.4 290 0.33 16.5 17.2 206.1 0.33 15.7 16.8 305.2 0.0 15 0.353 N 59.1 0.132 -7 0.33 15.3 15.5 257.8 0.33 15.6 16.3 235.2 0.33 15 16 219 0.0 16 0.344 N 58.8 0.109 -9.1 0.33 14.2 14.4 334.4 0.33 14.9 15.6 138.4 0.33 14.2 15.2 233.9 0.0 17 0.339 N 60 0.086 -11.5 0.33 13.5 13.6 223.4 0.33 13.9 14.7 183.3 0.33 13.1 14.2 272.8 0.0 18 0.371 N 59.3 0.06 -13.6 0.33 12.4 12.5 289.4 0.33 12.8 13.6 224.9 0.33 12.2 13.2 241.1 0.0 19 0.344 N 60.5 0.018 -16.4 0.33 11.4 11.4 244.5 0.33 11.8 12.6 175.4 0.33 11.2 12.1 239 0.0 20 0.358 N 61.4 0.016 -20.2 0.33 10.1 10.1 300.9 0.33 10.6 11.4 184.9 0.33 9.8 10.8 285.2 0.0 21 0.396 N 61.1 0.124 -23.4 0.33 8.9 8.8 277.7 0.33 9.4 10.2 187.9 0.33 8.7 9.6 243.7 0.0 22 0.361 N 61.6 0.1 -26.1 0.33 7.5 7.3 328 0.33 8.2 9 189.8 0.33 7.5 8.3 259.2 0.0 23 0.397 N 61.1 0.091 -26.8 0.33 6.4 6.1 241.4 0.33 6.8 7.7 207.4 0.33 6 6.9 286 0.0 24 0.396 N 61.6 0.083 -29.9 0.33 4.9 4.7 312 0.33 5.5 6.3 220.6 0.33 4.8 5.6 267.8 0.0 25 0.41 N 60.5 0.077 -30.1 0.33 3.5 3.2 265.3 0.33 4.2 5 156.3 0.33 3.5 4.2 219.5 0.0 26 0.409 N 62.5 0.071 -40 0.33 2.2 1.8 239.8 0.33 2.9 3.6 163.7 0.33 2.2 2.9 219.3 0.0 27 0.406 N 62 0.064 -42.8 0.33 0.6 0.2 296.5 0.33 1.3 2.2 192.4 0.33 0.6 1.2 288 0.0 28 0.368
133
EXP 9 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 60.3 0.059 -40.1 0.33 -0.9 -1.4 193.3 0.33 -0.2 0.6 142.4 0.33 -0.8 -0.3 168.4 0.0 29 0.353 N 65.6 0.053 -63.6 0.33 -2.8 -3.3 202.7 0.33 -2.3 -1.2 141.2 0.33 -3.2 -2.5 231 0.0 30 0.357
SW 64.2 0.051 -73.4 0.33 -4.9 -5.4 199.2 0.33 -4.4 -3.5 177.6 0.33 -4.8 -4.3 165.6 1.3 31 0.382 SW 64.3 0.049 -82.4 0.33 -7.1 -7.6 174.8 0.33 -6.8 -5.7 136.4 0.33 -7.5 -6.9 199.7 2.4 32 0.363 SW 70.8 0.044 -101.4 0.33 -9.5 -9.9 174.9 0.33 -9.5 -8.3 162.3 0.33 -10.2 -9.7 199.1 2.2 33 0.361 N 67.7 0.044 -107.4 0.33 -11.9 -12.4 177.6 0.33 -11.9 -10.8 140.6 0.33 -12.6 -12.3 181.5 0.0 34 0.399
SW 66.3 0.043 -112.6 0.33 -14.1 -14.8 152.3 0.33 -14.5 -13.3 130.3 0.33 -15.4 -15.1 185 1.9 35 0.341 SW 77.8 0.037 -125.8 0.33 -16.8 -17.4 173.7 0.33 -17.6 -16.2 164.7 0.33 -18.4 -18.2 205.4 2.9 36 0.328 SW 71.2 0.038 -123.9 0.33 -19.6 -20.2 183.3 0.33 -20.5 -19.1 158.3 0.33 -21.4 -21.3 203.8 2.3 37 0.388 SW 73.4 0.036 -127.8 0.33 -22.1 -22.9 169.1 0.33 -23.1 -21.8 145.8 0.33 -23.9 -24 178.3 1.7 38 0.352 SW 78.3 0.034 -132 0.33 -24.3 -25.2 157.3 0.33 -25.6 -24.4 146.9 0.33 -26.4 -26.8 190.1 3.0 39 0.381 SW 72.8 0.034 -128 0.33 -27 -27.8 170.4 0.33 -28.5 -27.2 151.5 0.33 -29.4 -29.8 208 3.1 40 0.328 SW 76.5 0.032 -133.1 0.33 -29.5 -30.4 164.6 0.33 -31.2 -29.9 144.6 0.33 -32.2 -32.7 191.2 1.7 41 0.367 SW 77.5 0.031 -139.9 0.33 -32.2 -33.2 121.5 0.33 -34 -32.7 104.8 0.33 -35 -35.7 139.9 3.5 42 0.384 SW 79.6 0.03 -185 0.33 -34.8 -35.8 121.2 0.33 -36.9 -35.6 115.5 0.33 -37.7 -38.5 138.4 3.5 43 0.34 SW 81.6 0.029 -185.8 0.33 -37.6 -38.7 129.4 0.33 -39.7 -38.4 112.3 0.33 -40.6 -41.5 144.5 3.0 44 0.383 SW 83.3 0.028 -185.5 0.33 -40 -41.3 117.1 0.33 -42.4 -41.1 105.1 0.33 -43.3 -44.4 142.4 4.7 45 0.363 SW 90.2 0.026 -186.6 0.33 -42.7 -43.9 125.9 0.33 -45.4 -44 119.1 0.33 -46.2 -47.4 155.7 3.6 46 0.376 SW 85.6 0.026 -185.1 0.33 -45 -46.4 115.3 0.33 -47.9 -46.6 102.5 0.33 -48.9 -50.3 146.2 3.9 47 0.303 SW 82.3 0.026 -186.1 0.33 -47.7 -49.1 130.2 0.33 -50.9 -49.5 120.3 0.33 -51.9 -53.4 166.3 3.1 48 0.385 SW 87.5 0.148 -185.2 0.33 -50.1 -51.6 121 0.33 -53.3 -52.1 110 0.33 -54.2 -55.9 137.1 4.2 49 0.353 SW 91.7 0.125 -185.9 0.33 -52.8 -54.4 133.5 0.33 -56.1 -54.9 121.6 0.33 -57 -58.8 158 3.8 50 0.362 SW 88.3 0.113 -185.3 0.33 -54.9 -56.7 112.5 0.33 -58.4 -57.2 96.7 0.33 -59.3 -61.4 145.3 4.2 51 0.337 SW 88.7 0.101 -186.3 0.33 -57.3 -59.1 120.5 0.33 -61 -59.8 113.9 0.33 -62 -64.1 156.1 4.1 52 0.356 SW 91.7 0.09 -185.4 0.33 -59.8 -61.6 127.6 0.33 -63.7 -62.5 121.6 0.33 -64.5 -66.7 156.1 3.7 53 0.329 SW 97.7 0.08 -185.8 0.33 -62.1 -64 123.9 0.33 -66 -64.9 109.7 0.33 -66.8 -69.2 152.8 3.9 54 0.356 SW 92.5 0.077 -185.5 0.33 -64.1 -66.2 114 0.33 -68.1 -67.1 93.8 0.33 -68.9 -71.5 141.3 4.3 55 0.346 SW 101.7 0.069 -186 0.33 -66.2 -68.3 111.8 0.33 -70.6 -69.6 119.9 0.33 -71.4 -74 156.3 3.9 56 0.344 SW 94.5 0.068 -185.6 0.33 -68.6 -70.7 127.5 0.33 -73.2 -72.2 126 0.33 -73.8 -76.6 163.4 2.2 57 0.329 SW 99 0.062 -185.9 0.33 -70.8 -73 121.2 0.33 -75.3 -74.5 111.7 0.33 -75.8 -78.8 141.1 4.1 58 0.352 SW 97.4 0.06 -185.8 0.33 -73 -75.2 120 0.33 -77.7 -76.9 122 0.33 -78.2 -81.2 163.3 3.1 59 0.325 SW 99.1 0.056 -185.8 0.33 -75.2 -77.5 125.4 0.33 -80 -79.2 119.5 0.33 -80.5 -83.6 160.5 3.3 60 0.37 SW 99 0.054 -185.8 0.33 -77.1 -79.5 112.3 0.33 -82.2 -81.4 115 0.33 -82.5 -85.8 152.3 4.3 61 0.343 SW 101.4 0.052 -185.8 0.33 -80.1 -82.4 163 0.33 -85.1 -84.3 161.7 0.33 -85.1 -88.4 179.2 3.6 62 0.331 SW 101.6 0.05 -186 0.33 -82 -84.5 121.4 0.33 -87 -86.4 111.6 0.33 -87.2 -90.7 163.7 4.4 63 0.353 SW 100.8 0.049 -185.7 0.33 -83.8 -86.4 107 0.33 -89 -88.6 126 0.33 -88.9 -92.6 138.7 3.7 64 0.354 SW 106.2 0.047 -186.1 0.33 -85.8 -88.4 115.5 0.33 -91.2 -90.7 120.7 0.33 -91.2 -94.9 169.9 3.8 65 0.335 SW 104.1 0.046 -185.8 0.33 -87.9 -90.6 130.9 0.33 -93.2 -92.9 129.5 0.33 -92.8 -96.7 139.7 3.0 66 0.354
134
EXP 9 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 104.2 0.045 -186.1 0.33 -89.7 -92.6 118.3 0.33 -95.1 -94.7 102.6 0.33 -95.1 -99 174.6 2.2 67 0.368 SW 109.3 0.043 -185.6 0.33 -91.4 -94.3 99.2 0.33 -97.1 -96.8 136 0.33 -96.8 -100.9 149.5 3.3 68 0.339 SW 105 0.043 -186.3 0.33 -93.2 -96.2 120.3 0.33 -98.8 -98.6 107.7 0.33 -98.4 -102.6 144.5 3.1 69 0.352 SW 109.4 0.042 -185.7 0.33 -95.1 -98.1 123.9 0.33 -100.5 -100.3 104 0.33 -100.2 -104.5 152.7 3.2 70 0.352 SW 106.9 0.042 -186.3 0.33 -96.9 -100 115.4 0.33 -102.5 -102.3 135.9 0.33 -102 -106.4 161.9 6.5 71 0.347 SW 112.6 0.041 -185.6 0.33 -98.6 -101.8 120.8 0.33 -104 -104.1 111.3 0.33 -103.4 -107.9 136.1 5.3 72 0.341 SW 106.4 0.041 -186.3 0.33 -100.2 -103.5 111.6 0.33 -105.9 -105.8 112.1 0.33 -105.4 -109.9 174.2 5.9 73 0.361 SW 111.3 0.04 -185.8 0.33 -102 -105.3 121.3 0.33 -107.5 -107.6 125.2 0.33 -106.8 -111.5 144 5.7 74 0.338 SW 107.3 0.04 -185.8 0.33 -103.6 -107 114.4 0.33 -109.5 -109.5 129.5 0.33 -108.8 -113.5 178.1 3.4 75 0.345 SW 109.3 0.039 -186 0.33 -105 -108.5 101.8 0.33 -110.7 -111 104.7 0.33 -109.9 -114.9 135.2 4.6 76 0.319 SW 103.5 0.04 -185.7 0.33 -106.9 -110.4 134.7 0.33 -112.6 -112.8 134 0.33 -111.7 -116.6 168.2 3.3 77 0.351 SW 111.7 0.038 -185.9 0.33 -108 -111.6 86.2 0.33 -113.9 -114.2 109.2 0.33 -112.8 -118 132.8 2.9 78 0.307 SW 104 0.04 -186.4 0.33 -109.9 -113.4 133.7 0.33 -115.6 -115.9 131.7 0.33 -114.5 -119.6 161.4 4.1 79 0.345 SW 113.2 0.039 -186 0.33 -111.2 -114.9 100.2 0.33 -117.3 -117.6 131.5 0.33 -116.1 -121.2 166.7 5.7 80 0.337 SW 111.7 0.039 -186.2 0.33 -112.4 -116.2 97.9 0.33 -118.4 -118.9 100.7 0.33 -117.2 -122.5 140.5 6.4 81 0.348 SW 113.9 0.04 -185.9 0.33 -114 -117.8 124 0.33 -120 -120.4 131 0.33 -118.8 -124.1 164.2 7.2 82 0.251 SW 119.1 0.04 -185.9 0.33 -115.3 -119.2 101.9 0.33 -121.5 -121.9 119.6 0.33 -120.3 -125.7 172.2 6.0 83 0.373 SW 113.3 0.04 -186.4 0.33 -116.5 -120.4 94.5 0.33 -122.5 -123.2 115.8 0.33 -120.9 -126.6 103.1 4.3 84 0.314 SW 112.7 0.04 -186.1 0.33 -118 -122 129.2 0.33 -123.9 -124.5 116.3 0.33 -122.5 -128 167.2 5.2 85 0.373 SW 109.6 0.04 -186.5 0.33 -119 -123.2 89.1 0.33 -125.2 -125.8 103.8 0.33 -123.9 -129.5 167.4 4.4 86 0.321 SW 118.6 0.039 -186.3 0.33 -120.4 -124.6 121.1 0.33 -126.3 -127 107.1 0.33 -124.9 -130.7 146.7 4.2 87 0.358 SW 108.7 0.042 -186.4 0.33 -121.3 -125.6 75.8 0.33 -127.5 -128.3 120 0.33 -126 -131.8 142 3.4 88 0.262 SW 120 0.041 -185.8 0.33 -122.7 -126.9 115.7 0.33 -129 -129.7 136.2 0.33 -127.5 -133.2 178.6 4.5 89 0.351 SW 113.3 0.043 -186.2 0.33 -123.6 -127.9 79.6 0.33 -130 -130.8 112.4 0.33 -128.4 -134.3 144.4 4.3 90 0.256 SW 124.4 0.042 -186 0.33 -125 -129.2 120.1 0.33 -131.3 -132 119.2 0.33 -129.7 -135.7 173.6 4.4 91 0.315 SW 123.1 0.049 -186.3 0.33 -125.9 -130.3 88.6 0.33 -132.1 -133.2 128.9 0.33 -130.1 -136.3 93.4 4.0 92 0.266 SW 133.6 0.049 -186 0.33 -127.2 -131.6 115.3 0.33 -133.7 -134.3 107.2 0.33 -132.4 -138.2 254.4 4.0 93 0.308 SW 123.3 0.052 -186.3 0.33 -127.9 -132.4 72.8 0.33 -134.6 -135.3 100.1 0.33 -133.1 -139.3 149.5 4.3 94 0.314 SW 128.6 0.049 -186.5 0.33 -128.9 -133.4 93.2 0.33 -135.6 -136.4 119.5 0.33 -133.9 -140.2 144.7 8.1 95 0.332 SW 105.4 0.049 -185.9 0.33 -130.3 -134.8 129.2 0.33 -136.8 -137.5 119.8 0.33 -135.2 -141.4 179.2 7.6 96 0.313 SW 112.2 0.046 -186.3 0.33 -131.1 -135.7 84.1 0.33 -137.8 -138.7 133.5 0.33 -136 -142.4 152.4 7.6 97 0.303 SW 114.2 0.049 -186.4 0.33 -132.1 -136.7 96.9 0.33 -138.8 -139.7 110.7 0.33 -137 -143.4 168.6 6.5 98 0.269 SW 126.8 0.054 -186.2 0.33 -133 -137.7 100.5 0.33 -139.6 -140.6 104.8 0.33 -137.8 -144.3 149.4 6.7 99 0.311 SW 120.3 0.056 -186.2 0.33 -134 -138.7 102.9 0.33 -140.5 -141.6 117.7 0.33 -138.5 -145.1 139.7 5.6 100 0.269 SW 120.5 0.056 -186.4 0.33 -135.1 -139.8 101.5 0.33 -141.8 -142.8 156.6 0.33 -139.8 -146.3 200.4 5.4 101 0.291 SW 116 0.056 -186.4 0.33 -135.8 -140.6 90.6 0.33 -142.5 -143.6 101.8 0.33 -140.4 -147.1 146.9 5.4 102 0.33 SW 115.3 0.056 -186.1 0.33 -136.9 -141.7 117.5 0.33 -143.4 -144.6 127.8 0.33 -141.2 -147.9 152.6 4.3 103 0.267 SW 113.1 0.056 -185.8 0.33 -138 -142.8 122 0.33 -144.4 -145.6 139.1 0.33 -142.2 -148.9 176.2 3.8 104 0.357
135
EXP 9 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 108.5 0.057 -186.5 0.33 -138.7 -143.6 72 0.33 -145.4 -146.6 143.9 0.33 -143.1 -149.8 181.9 3.9 105 0.306 SW 100.2 0.058 -186.1 0.33 -139.6 -144.5 104.1 0.33 -146.2 -147.5 129.2 0.33 -143.9 -150.7 159.1 4.0 106 0.346 SW 101.8 0.059 -186.8 0.33 -140.4 -145.3 94.9 0.33 -147.1 -148.4 124.3 0.33 -144.7 -151.5 172.9 5.8 107 0.288 SW 99.7 0.059 -186.6 0.33 -141.2 -146.2 100.1 0.33 -147.8 -149.2 113.7 0.33 -145.4 -152.3 162.1 7.4 108 0.303 SW 103.8 0.058 -186.7 0.33 -141.9 -147 93.9 0.33 -148.4 -149.8 91.9 0.33 -146.2 -153.1 165.8 4.9 109 0.248 SW 101.3 0.058 -186.2 0.33 -142.7 -147.8 94.4 0.33 -149.3 -150.6 136.5 0.33 -146.9 -153.9 173.8 5.8 110 0.269 SW 102.4 0.057 -186.6 0.33 -143.6 -148.7 104.9 0.33 -150.5 -151.8 181.3 0.33 -148 -154.9 215.1 6.4 111 0.251 SW 102.7 0.057 -186.4 0.33 -144.5 -149.6 109.3 0.33 -151.5 -152.7 153.5 0.33 -149.2 -156.1 239.2 5.8 112 0.242 SW 103.3 0.056 -186.5 0.33 -145.1 -150.2 78.8 0.33 -152 -153.6 149 0.33 -149.4 -156.6 123.6 7.7 113 0.273 SW 102.4 0.055 -186.5 0.33 -145.6 -150.8 64.5 0.33 -152.6 -154.1 103 0.33 -150.2 -157.3 183.7 5.6 114 0.283 SW 100 0.056 -186.9 0.33 -146.1 -151.3 60.3 0.33 -153.2 -154.8 133.1 0.33 -150.6 -157.8 143.7 6.1 115 0.225 SW 98.9 0.055 -186.7 0.33 -147.2 -152.3 132.4 0.33 -154.1 -155.6 150.7 0.33 -151.4 -158.6 195.6 5.7 116 0.354 SW 97.2 0.054 -187 0.33 -147.8 -153 83.1 0.33 -154.7 -156.3 135.4 0.33 -152.2 -159.4 199.6 2.9 117 0.237 SW 97.3 0.054 -186.3 0.33 -148.5 -153.7 93.2 0.33 -155.7 -157.1 155.7 0.33 -153.2 -160.4 249.1 4.6 118 0.198 SW 102.3 0.051 -187.1 0.33 -149.1 -154.3 82.7 0.33 -156.5 -157.9 158.8 0.33 -154.1 -161.3 231.9 3.0 119 0.224 SW 96.1 0.052 -186.5 0.33 -150.2 -155.4 146 0.33 -157.5 -158.9 198.8 0.33 -155 -162.3 260.7 4.2 120 0.182 SW 96.8 0.066 -186.7 0.42 -151.2 -156.1 78.7 0.17 -165 -162.5 746.7 0.17 -179.1 -183.7 5418.5 4.1 121 0.222
EXP 10 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 52.3 1 15.3 0.33 23.2 24 658.5 0.33 23.3 24.1 578.3 0.33 22.7 24.2 514.3 0.0 1 0.508 N 56.4 1 12.4 0.33 23 23.5 192.7 0.33 23.2 23.8 103.5 0.33 22.5 23.7 202.9 0.0 2 0.469 N 56.9 1 10.1 0.33 22.7 23.2 174.1 0.33 22.7 23.3 198.4 0.33 22 23.3 203 0.0 3 0.498 N 56.9 1 8.5 0.33 21.8 22.3 395.9 0.33 22.1 22.8 237.8 0.33 21.4 22.7 289.6 0.0 4 0.514 N 57.4 1 6.7 0.33 21.3 21.7 258.4 0.33 21.6 22.2 214.1 0.33 20.9 22.2 193.2 0.0 5 0.573 N 58.3 1 4.9 0.33 20.7 21.1 254.8 0.33 21.1 21.7 144.2 0.33 20.3 21.6 235.3 0.0 6 0.409 N 59.5 1 2.8 0.33 20 20.4 243.5 0.33 20.3 21 226.2 0.33 19.6 20.8 263.2 0.0 7 0.622 N 59.2 1 0.3 0.33 19.2 19.6 296.4 0.33 19.6 20.3 189.3 0.33 18.9 20.1 226.1 0.0 8 0.703 N 59.8 1 -2.4 0.33 18.1 18.5 327.1 0.33 18.4 19.2 273.4 0.33 17.7 19 324.8 0.0 9 0.639 N 58.4 1 -5.1 0.33 17.2 17.4 305.2 0.33 17.7 18.4 160.4 0.33 16.9 18.1 238 0.0 10 0.62 N 60.3 1 -8.3 0.33 16.2 16.4 271.7 0.33 16.5 17.4 236.3 0.33 15.7 16.9 310.5 0.0 11 0.682 N 59.5 1 -11 0.33 15 15.2 312.3 0.33 15.4 16.2 240.8 0.33 14.7 15.8 266.2 0.0 12 0.67 N 60.8 1 -13.1 0.33 13.9 14.1 271.4 0.33 14.4 15.1 194.5 0.33 13.7 14.8 224 0.0 13 0.431 N 60.1 1.034 -18.1 0.33 12.6 12.8 252.5 0.33 13.2 14 180.6 0.33 12.5 13.6 236.1 0.0 14 0.58 N 62.1 0.376 -25 0.33 11.1 11.3 246.4 0.33 11.7 12.6 177.7 0.33 11 12.1 231.9 0.0 15 0.594 N 63 0.248 -34.1 0.33 9.7 9.8 208.4 0.33 10.1 11.1 161.7 0.33 9.3 10.4 219.4 0.0 16 0.772 N 64.5 0.197 -44.2 0.33 8.1 8.1 203.6 0.33 8.6 9.5 155.2 0.33 7.8 8.8 195.5 0.0 17 0.57 N 63.3 0.163 -50.6 0.33 5.7 5.9 228.1 0.33 6 7.3 185.8 0.33 5.1 6.3 246.1 0.0 18 0.578
136
EXP 10 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 66.7 0.132 -68.8 0.33 3.8 3.8 234.9 0.33 4 5.2 194.9 0.33 3.1 4.1 245.8 0.0 19 0.664 N 63.6 0.121 -59.3 0.33 1.6 1.5 239.8 0.33 2 3.1 171.9 0.33 1.1 2 215.7 0.0 20 0.509 N 64 0.108 -67.5 0.33 -0.5 -0.7 241.4 0.33 -0.4 0.8 208.5 0.33 -1.3 -0.5 268.8 0.0 21 0.625 N 65.3 0.096 -65.9 0.33 -2.5 -2.8 199.1 0.33 -2.1 -1.1 130.2 0.33 -3 -2.4 174.8 0.0 22 0.597 N 64.9 0.088 -81.3 0.33 -4.6 -4.9 155.4 0.33 -4.6 -3.3 135.8 0.33 -5.5 -4.9 181.6 0.0 23 0.528 N 71.6 0.076 -103.9 0.33 -7.5 -7.7 200.7 0.33 -7.6 -6.2 167.8 0.33 -8.6 -7.9 212.7 0.0 24 0.678 N 65.7 0.075 -109.3 0.33 -9.9 -10.3 152.3 0.33 -10.3 -8.8 127.4 0.33 -11.5 -11 184.5 0.0 25 0.672 N 79.4 0.062 -130.5 0.33 -12.9 -13.2 171 0.33 -13.8 -12.1 171.4 0.33 -14.9 -14.4 203.5 0.0 26 0.513
SW 77.2 0.022 -133 0.33 -16 -16.3 181.4 0.33 -17.1 -15.4 160.7 0.33 -18.3 -17.9 209.1 1.8 27 0.43 SW 77.4 0.022 -136.8 0.33 -18.9 -19.3 173.3 0.33 -20.2 -18.6 159.2 0.33 -21.3 -21.1 192.8 1.9 28 0.593 SW 76.6 0.022 -139.7 0.33 -22.1 -22.5 133.7 0.33 -23.6 -22 125.3 0.33 -24.7 -24.6 154.1 2.1 29 0.65 SW 85.8 0.021 -185.4 0.33 -25.1 -25.5 128.3 0.33 -27.1 -25.4 130.2 0.33 -28.1 -28.2 158.8 3.7 30 0.561 SW 82.5 0.022 -185.9 0.33 -27.9 -28.5 127.9 0.33 -30.2 -28.5 116.9 0.33 -31.5 -31.7 161 2.6 31 0.6 SW 86 0.021 -186 0.33 -30.9 -31.6 133.2 0.33 -33.3 -31.7 121.2 0.33 -34.6 -35.1 157 4.1 32 0.594 SW 88.5 0.021 -185.1 0.33 -33.8 -34.6 130.2 0.33 -36.7 -35 129.6 0.33 -38.1 -38.7 170.9 4.1 33 0.575 SW 85 0.021 -185.8 0.33 -36.5 -37.4 126.2 0.33 -39.5 -37.9 116.8 0.33 -40.8 -41.7 148.8 3.0 34 0.726 SW 89.5 0.021 -185.3 0.33 -39.4 -40.3 129.3 0.33 -42.9 -41.1 126.1 0.33 -44.4 -45.3 182 2.9 35 0.532 SW 89.9 0.021 -185.6 0.33 -42 -43.1 126.6 0.33 -45.6 -43.9 115 0.33 -47.1 -48.3 153.4 5.5 36 0.502 SW 94.3 0.021 -185.2 0.33 -44.8 -45.9 128.8 0.33 -48.7 -47 125.3 0.33 -50.1 -51.5 167.5 4.8 37 0.397 SW 94.5 0.021 -185.4 0.33 -47.3 -48.5 122 0.33 -51.5 -49.8 122.5 0.33 -52.9 -54.4 158.7 3.3 38 0.389 SW 94 0.021 -185.1 0.33 -50 -51.2 126.5 0.33 -54.2 -52.6 117.3 0.33 -55.5 -57.2 156 3.7 39 0.374 SW 99.4 0.02 -185.6 0.33 -52.5 -53.8 123.5 0.33 -57 -55.4 119 0.33 -58.5 -60.3 172.7 6.1 40 0.398 SW 97 0.021 -185.5 0.33 -55 -56.4 126.4 0.33 -59.5 -58.1 119 0.33 -60.6 -62.8 141.2 5.0 41 0.387 SW 99.7 0.021 -185.6 0.33 -57.7 -59.1 131.7 0.33 -62.3 -60.9 129.1 0.33 -63.3 -65.5 162.6 5.7 42 0.412 SW 98.6 0.021 -185.6 0.33 -59.8 -61.4 109.9 0.33 -64.6 -63.3 107 0.33 -65.7 -68.1 154.4 4.3 43 0.424 SW 99.6 0.021 -185.6 0.33 -62.4 -64 132.7 0.33 -67.3 -65.9 122.1 0.33 -68.4 -70.8 166.2 4.1 44 0.404 SW 100.1 0.021 -185.7 0.33 -64.5 -66.3 110.1 0.33 -69.7 -68.4 116.5 0.33 -70.8 -73.4 161.6 5.0 45 0.437 SW 99.4 0.021 -185.7 0.33 -67.1 -68.9 135.6 0.33 -72 -70.8 119.7 0.33 -72.9 -75.7 148.9 4.7 46 0.426 SW 101.6 0.021 -185.6 0.33 -69.4 -71.3 122.9 0.33 -74.7 -73.5 131.6 0.33 -75.5 -78.3 171.5 3.8 47 0.348 SW 99.6 0.021 -185.9 0.33 -71.5 -73.5 116.9 0.33 -76.9 -75.8 119 0.33 -77.5 -80.6 149.5 5.1 48 0.432 SW 103.2 0.021 -185.8 0.33 -73.8 -75.9 126.9 0.33 -79.3 -78.2 120.9 0.33 -80 -83 168.1 3.2 49 0.403 SW 102.6 0.021 -185.7 0.33 -76.2 -78.3 128.7 0.33 -81.8 -80.8 143 0.33 -82.3 -85.5 166.6 4.4 50 0.419 SW 109.2 0.021 -185.7 0.33 -78.9 -80.9 147.3 0.33 -84.5 -83.5 143.8 0.33 -85.1 -88.3 192.7 4.2 51 0.451 SW 107.7 0.022 -186.2 0.33 -80.9 -83.2 123.6 0.33 -86.6 -85.7 116.7 0.33 -87.2 -90.7 169.8 4.3 52 0.498 SW 112.3 0.021 -185.8 0.33 -83.1 -85.5 126.7 0.33 -88.9 -88.1 132.5 0.33 -89.2 -92.9 161.7 6.2 53 0.456 SW 109.1 0.022 -185.9 0.33 -85 -87.4 109.9 0.33 -91.1 -90.3 133.6 0.33 -91.3 -95 164.7 5.6 54 0.404 SW 112.4 0.022 -185.7 0.33 -86.9 -89.5 118 0.33 -92.9 -92.3 109.4 0.33 -93 -97 149.8 6.2 55 0.386 SW 117.7 0.022 -186 0.33 -88.8 -91.3 106.1 0.33 -95.1 -94.4 132.3 0.33 -95.3 -99.2 176.6 6.9 56 0.396
137
EXP 10 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 113.2 0.023 -186.2 0.33 -90.4 -93.1 103.6 0.33 -96.7 -96.2 103.1 0.33 -96.9 -101 147.2 5.4 57 0.449 SW 118.5 0.023 -185.9 0.33 -92 -94.8 98.2 0.33 -98.5 -98 113.5 0.33 -98.6 -102.9 154.5 4.4 58 0.522 SW 122.1 0.023 -186 0.33 -93.9 -96.7 113.5 0.33 -100.5 -99.9 116 0.33 -100.8 -105 182 6.3 59 0.553 SW 119.5 0.024 -185.9 0.33 -95.2 -98.2 87.2 0.33 -101.9 -101.4 93.5 0.33 -102.2 -106.7 145.6 2.5 60 0.378 SW 122.2 0.024 -185.6 0.33 -96.9 -99.7 95.5 0.33 -104 -103.4 130 0.33 -104.4 -108.8 186.2 3.4 61 0.303 SW 130.3 0.025 -186 0.33 -98.3 -101.3 94.2 0.33 -105.5 -105 105.3 0.33 -105.8 -110.4 152 3.2 62 0.426 SW 132.2 0.025 -186.1 0.33 -99.6 -102.7 84.8 0.33 -106.9 -106.4 92 0.33 -107.3 -112.1 157 4.2 63 0.343 SW 128.6 0.026 -186.4 0.33 -101.2 -104.3 98.6 0.33 -108.5 -108 106.7 0.33 -108.8 -113.6 156 8.1 64 0.242 SW 135.1 0.026 -186.4 0.33 -102.7 -105.8 98.9 0.33 -110.2 -109.7 116.6 0.33 -110.5 -115.3 171.1 4.4 65 0.398 SW 127.5 0.027 -186 0.33 -104 -107.2 82.3 0.33 -111.6 -111.2 103.8 0.33 -111.9 -116.9 158.5 4.9 66 0.334 SW 135 0.027 -185.9 0.33 -105.5 -108.7 97.3 0.33 -113.3 -112.8 118.1 0.33 -113.5 -118.5 175.3 5.7 67 0.261 SW 132.5 0.028 -185.9 0.33 -106.7 -110 79.6 0.33 -114.4 -114.1 91.1 0.33 -114.7 -119.9 148.5 3.1 68 0.272 SW 135.3 0.028 -186.1 0.33 -108.3 -111.5 107.2 0.33 -115.9 -115.5 105.3 0.33 -116.1 -121.4 167.3 5.0 69 0.307 SW 137.7 0.029 -185.8 0.33 -109.5 -112.8 80.9 0.33 -117.4 -117 116.8 0.33 -117.6 -122.9 171 8.1 70 0.269 SW 134.2 0.03 -186.2 0.33 -110.7 -114.1 85 0.33 -118.8 -118.4 106.6 0.33 -118.9 -124.3 166.8 4.3 71 0.298 SW 136.2 0.031 -186.2 0.33 -111.9 -115.3 80.5 0.33 -119.9 -119.7 96.3 0.33 -120 -125.5 149.1 8.4 72 0.341 SW 134.5 0.032 -185.8 0.33 -113.4 -116.8 103.1 0.33 -121.3 -121.1 113.3 0.33 -121.3 -126.9 171.3 4.4 73 0.266 SW 128.4 0.033 -186 0.33 -114.4 -118 76.4 0.33 -122.5 -122.4 108.8 0.33 -122.2 -127.9 141.8 3.7 74 0.409 SW 134.4 0.034 -186 0.33 -116 -119.5 111.1 0.33 -123.9 -123.8 121.9 0.33 -123.5 -129.2 164.7 4.0 75 0.4 SW 131.1 0.035 -186.4 0.33 -117 -120.7 84.8 0.33 -124.9 -124.9 89.4 0.33 -124.6 -130.4 154.3 6.3 76 0.557 SW 133.3 0.037 -185.8 0.33 -118.5 -122.1 103.7 0.33 -126.4 -126.4 138.8 0.33 -125.8 -131.6 169.8 3.9 77 0.263 SW 130 0.037 -185.9 0.33 -119.7 -123.4 95 0.33 -127.4 -127.7 117.8 0.33 -126.6 -132.6 137.2 4.5 78 0.321 SW 138.1 0.038 -185.9 0.33 -120.9 -124.7 95.6 0.33 -128.7 -128.8 110.6 0.33 -128 -133.9 175.9 4.5 79 0.333 SW 125 0.039 -186.2 0.33 -122 -125.9 87.3 0.33 -129.6 -130 113.2 0.33 -128.7 -134.8 137.8 5.6 80 0.421 SW 121 0.038 -186.1 0.33 -123.2 -127.2 104.1 0.33 -130.8 -131.1 112.6 0.33 -129.8 -135.9 158.7 5.1 81 0.445 SW 120.5 0.037 -185.9 0.33 -124.5 -128.5 102.2 0.33 -132.1 -132.5 145.1 0.33 -130.8 -136.9 157.7 4.1 82 0.365 SW 121.1 0.037 -186 0.33 -125.7 -129.7 94.8 0.33 -133.1 -133.8 133.3 0.33 -131.6 -137.8 133.1 7.1 83 0.56 SW 127.6 0.038 -186.2 0.33 -126.8 -130.9 99.2 0.33 -134 -134.7 104.2 0.33 -132.6 -138.8 161.2 4.3 84 0.351 SW 122.6 0.038 -185.7 0.33 -128.3 -132.4 134 0.33 -135.3 -136 147.2 0.33 -133.7 -139.9 165 4.6 85 0.559 SW 123.6 0.038 -186.1 0.33 -129.1 -133.3 73.5 0.33 -136.4 -137.1 126.2 0.33 -134.7 -141 161.5 8.4 86 0.417 SW 117.5 0.039 -186.3 0.33 -130.4 -134.7 124 0.33 -137.1 -138.1 107.2 0.33 -135.2 -141.7 118.8 4.2 87 0.403 SW 115.1 0.039 -186.7 0.33 -131.5 -135.8 101.4 0.33 -138.3 -139.3 153.3 0.33 -136.3 -142.7 159.1 3.8 88 0.455 SW 109.4 0.039 -185.9 0.33 -132.7 -137 114.1 0.33 -139.5 -140.6 157.4 0.33 -137.2 -143.7 160.9 3.7 89 0.432 SW 121.5 0.039 -186.1 0.33 -133.6 -138.1 100.2 0.33 -140.3 -141.4 108.4 0.33 -138.2 -144.7 166.6 7.6 90 0.46 SW 127.2 0.042 -185.4 0.33 -134.7 -139.2 111.3 0.33 -141.2 -142.5 143.8 0.33 -138.8 -145.4 125.8 3.1 91 0.49 SW 125.1 0.045 -185.9 0.33 -135.4 -140.1 75.7 0.33 -142.2 -143.5 133.2 0.33 -139.9 -146.5 180.2 6.7 92 0.57 SW 143.1 0.048 -186.1 0.33 -136.5 -141.1 110.2 0.33 -143.2 -144.5 143.7 0.33 -140.8 -147.4 167.1 4.1 93 0.657 SW 119.1 0.052 -186.1 0.33 -137.6 -142.3 124.2 0.33 -144.2 -145.5 133.7 0.33 -141.9 -148.5 184.8 5.1 94 0.526
138
EXP 10 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 133.7 0.051 -186.4 0.33 -138.2 -143 69.1 0.33 -145.4 -146.3 101.8 0.33 -143.8 -150.2 281.2 4.8 95 0.434 SW 124.6 0.053 -186.2 0.33 -139.3 -144.1 115.7 0.33 -146.4 -147.4 158.7 0.33 -144.4 -151.2 172.1 4.0 96 0.463 SW 124.2 0.053 -186.1 0.33 -140.1 -145 97.6 0.33 -147.1 -148.3 122.8 0.33 -145.1 -152 169.9 5.8 97 0.409 SW 123.7 0.053 -186.3 0.33 -141.4 -146.3 153.6 0.33 -148 -149.1 121.3 0.33 -146 -152.9 192.4 7.3 98 0.492 SW 122.7 0.053 -186.3 0.33 -141.9 -147 71 0.33 -148.9 -150.2 151.4 0.33 -146.6 -153.6 164.4 8.6 99 0.443 SW 123.9 0.052 -186.4 0.33 -142.7 -147.7 89.8 0.33 -149.6 -150.9 111 0.33 -147.4 -154.4 179.3 4.9 100 0.475 SW 124.1 0.052 -186.5 0.33 -143.4 -148.5 99.4 0.33 -150 -151.4 74.1 0.33 -148 -155.1 161.7 3.5 101 0.3 SW 126.1 0.052 -186.4 0.33 -144.1 -149.2 79.9 0.33 -151.2 -152.4 168 0.33 -149.1 -156.1 231 4.5 102 0.336 SW 120.4 0.052 -186.2 0.33 -145.2 -150.3 140.8 0.33 -152 -153.3 142.2 0.33 -149.8 -156.9 199.4 9.4 103 0.355 SW 122.2 0.052 -186.1 0.33 -145.9 -151.1 94.2 0.33 -152.9 -154.2 150 0.33 -150.6 -157.8 204.3 4.2 104 0.282 SW 123.8 0.052 -186.3 0.33 -146.7 -152 127.9 0.33 -153.4 -154.8 105.7 0.33 -151.2 -158.4 176.3 5.4 105 0.367 SW 121.2 0.052 -186.1 0.33 -147.4 -152.7 90.1 0.33 -154.4 -155.7 156.6 0.33 -152.2 -159.4 244.8 7.1 106 0.325 SW 121.3 0.052 -186.1 0.33 -148 -153.3 90.4 0.33 -155 -156.4 121.1 0.33 -152.7 -160 182.5 3.3 107 0.294 SW 124.8 0.051 -186.3 0.33 -148.9 -154.2 120.1 0.33 -155.9 -157.2 137.1 0.33 -153.7 -161 249.8 4.7 108 0.226 SW 126.5 0.05 -186.5 0.42 -149.5 -154.9 103.8 0.42 -159.7 -158.2 115.4 0.17 -174.8 -180 4801.7 5.0 109 0.327 SW 127.8 0.023 -186.3 0.42 -152.7 -155.6 43.8 0.42 -179.2 -173.6 3656.4 0.17 -182 -185.9 21329.9 3.0 110 0.223 SW 120.2 0.051 -186.2 -156.9 -183.2 -186.8 4.4 111 0.127
EXP 11 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 53.8 1 11.5 0.33 22.6 23.5 759 0.33 22.7 23.7 668.1 0.33 22 23.7 689.5 0.0 1 0.354 N 55.1 1 9.5 0.33 22.1 22.7 331.6 0.33 22.3 23 254.5 0.33 21.6 22.9 311.3 0.0 2 0.302 N 56.9 1 7.4 0.33 21.6 22.1 269.5 0.33 21.7 22.4 191.6 0.33 21 22.3 255.3 0.0 3 0.358 N 55.8 1 5.2 0.33 20.9 21.3 300.2 0.33 21.1 21.8 215.4 0.33 20.4 21.6 245.7 0.0 4 0.371 M 56.1 1 3.1 0.33 20.1 20.6 266.2 0.33 20.1 20.9 297.1 0.33 19.3 20.7 351.3 0.0 5 0.375 M 56.7 1 0.6 0.33 19 19.5 355.6 0.33 19.4 20.1 205.3 0.33 18.6 19.9 244.2 0.0 6 0.307 M 57.7 1 -2.6 0.33 18 18.4 321.1 0.33 18.4 19.2 204.6 0.33 17.5 18.8 307.3 0.0 7 0.372 M 57.8 1 -6.9 0.33 16.7 17.2 323 0.33 16.9 17.9 306.8 0.33 16.2 17.5 325.2 0.0 8 0.375 M 57.5 1 -10.9 0.33 15.3 15.7 343.8 0.33 15.8 16.6 244.7 0.33 15.2 16.4 252.2 0.0 9 0.394 M 60.3 1 -15 0.33 13.9 14.2 260.8 0.33 14.3 15.2 205 0.33 13.4 14.7 288.6 0.0 10 0.309 M 59.2 1 -26.7 0.33 12.1 12.5 295.8 0.33 12.3 13.4 261 0.33 11.4 12.7 323.8 0.0 11 0.395 M 60 1 -31.2 0.33 10.3 10.5 254.4 0.33 10.8 11.8 162.3 0.33 9.9 11 220.1 0.0 12 0.369 M 61.6 1 -45 0.33 8.1 8.4 297.3 0.33 8.5 9.7 249.7 0.33 7.7 8.9 287.8 0.0 13 0.33 M 59.7 1 -44.2 0.33 6 6.1 225.4 0.33 6.2 7.5 176.6 0.33 5.1 6.3 258.4 0.0 14 0.338 M 63.9 1 -65.8 0.33 3.2 3.4 276.9 0.33 3.4 5 209.8 0.33 2.2 3.4 289.7 0.0 15 0.414
139
EXP 11 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P M 62.7 0.652 -67.9 0.33 0.7 0.7 277.5 0.33 1 2.4 219.4 0.33 0.1 1 245.8 0.0 16 0.322
SW 63.7 0.05 -68.7 0.33 -2.2 -2.2 313.4 0.33 -2 -0.5 259.1 0.33 -3.1 -2.1 337.2 3.3 17 0.417 SW 64.5 0.049 -67.9 0.33 -4.6 -4.8 180.9 0.33 -4.7 -3.2 153.9 0.33 -5.8 -5 203.5 3.1 18 0.346 SW 68.5 0.046 -106.4 0.33 -7.8 -7.9 196.5 0.33 -8.1 -6.3 165.3 0.33 -9.4 -8.5 220.6 1.9 19 0.368 SW 73.5 0.044 -122.1 0.33 -11.5 -11.5 211.1 0.33 -12.3 -10.3 201.4 0.33 -13.5 -12.6 243.6 2.7 20 0.309 SW 74.9 0.043 -132.8 0.33 -15.2 -15.3 175.4 0.33 -16.4 -14.3 163.3 0.33 -17.8 -17 208.5 2.4 21 0.388 SW 76.8 0.042 -164.7 0.33 -18.6 -18.8 144.2 0.33 -20.2 -18.1 133.8 0.33 -21.8 -21.3 182.5 3.5 22 0.36 SW 84.8 0.039 -185.5 0.33 -22.8 -22.9 174.6 0.33 -24.6 -22.3 159 0.33 -26.2 -25.9 200.7 3.4 23 0.371 SW 83.5 0.039 -185 0.33 -26.1 -26.5 151.3 0.33 -28.5 -26.3 145.4 0.33 -30.3 -30.2 196.7 3.1 24 0.315 SW 84.3 0.039 -184.9 0.33 -29.8 -30.2 162.2 0.33 -32.4 -30.2 149.2 0.33 -34.2 -34.3 190.4 3.2 25 0.319 SW 87.9 0.037 -185.3 0.33 -33.6 -34.1 170.4 0.33 -36.6 -34.3 160.3 0.33 -38.4 -38.7 210.7 3.3 26 0.334 SW 87.9 0.037 -185 0.33 -37 -37.6 155.5 0.33 -40.4 -38.2 151.2 0.33 -42.2 -42.8 197.1 2.7 27 0.269 SW 91.4 0.036 -185.5 0.33 -40.4 -41.1 156.1 0.33 -44.1 -41.9 151.1 0.33 -45.9 -46.7 196.6 3.5 28 0.309 SW 93.8 0.036 -185.3 0.33 -43.8 -44.6 160.1 0.33 -48 -45.7 160.1 0.33 -49.8 -50.8 209.9 4.7 29 0.308 SW 96.5 0.035 -185.1 0.33 -47 -48 154.4 0.33 -51.3 -49.2 142 0.33 -53.2 -54.5 196.8 3.9 30 0.297 SW 96.9 0.035 -185.3 0.33 -50.2 -51.3 154.7 0.33 -54.8 -52.7 150.2 0.33 -56.6 -58.1 197.4 3.6 31 0.354 SW 102.3 0.034 -185.4 0.33 -53.8 -54.8 171.5 0.33 -58.5 -56.4 164 0.33 -60.2 -61.8 211.4 4.4 32 0.328 SW 99.4 0.035 -185.1 0.33 -56.7 -58 149.3 0.33 -61.8 -59.8 146.9 0.33 -63.5 -65.4 204.9 4.6 33 0.346 SW 100 0.035 -185.3 0.33 -59.7 -61.1 153.2 0.33 -64.8 -63 144.1 0.33 -66.4 -68.6 186.2 2.9 34 0.31 SW 104.5 0.034 -185.2 0.33 -62.9 -64.3 161.8 0.33 -68.1 -66.3 155.6 0.33 -69.5 -71.8 197.5 4.6 35 0.337 SW 100 0.035 -185.3 0.33 -65.5 -67.1 143 0.33 -71.1 -69.4 146.4 0.33 -72.6 -75 202.1 3.4 36 0.324 SW 104.2 0.034 -185.4 0.33 -68.8 -70.4 171.1 0.33 -74.1 -72.5 149.8 0.33 -75.5 -78.1 197.9 4.4 37 0.355 SW 103.8 0.035 -185.1 0.33 -71.4 -73.2 142.2 0.33 -77.3 -75.7 169.1 0.33 -78.5 -81.3 205.8 4.7 38 0.381 SW 105 0.035 -184.9 0.33 -74.3 -76.2 162 0.33 -80 -78.6 142.2 0.33 -81.1 -84.1 194.2 4.4 39 0.327 SW 106.2 0.035 -185.3 0.33 -77.1 -78.9 150.9 0.33 -83.2 -81.8 172.3 0.33 -84.1 -87.2 211.4 5.7 40 0.318 SW 110.7 0.034 -185 0.33 -79.5 -81.6 147.5 0.33 -85.7 -84.3 130.9 0.33 -86.9 -90.1 206.9 4.6 41 0.339 SW 106.2 0.035 -185.5 0.33 -82.5 -84.6 171.5 0.33 -88.5 -87.2 161.7 0.33 -89.3 -92.7 190.1 5.8 42 0.326 SW 111 0.035 -185.3 0.33 -84.6 -86.9 126.8 0.33 -91.3 -90 156.3 0.33 -92.2 -95.7 219.8 5.2 43 0.328 SW 111.4 0.036 -185.3 0.33 -87 -89.4 140.2 0.33 -93.6 -92.5 138.6 0.33 -94.5 -98.3 196.9 5.8 44 0.317 SW 113.8 0.036 -185.4 0.33 -89.5 -91.9 149.5 0.33 -96.4 -95.1 156.1 0.33 -97.2 -101.1 220.9 4.8 45 0.341 SW 116.3 0.036 -185.5 0.33 -91.7 -94.3 142.1 0.33 -98.5 -97.5 141.9 0.33 -99.1 -103.3 181.7 5.2 46 0.289 SW 117 0.037 -185.8 0.33 -93.9 -96.5 129.5 0.33 -101 -100 157.2 0.33 -101.7 -105.8 213.9 6.1 47 0.256 SW 115.9 0.038 -185.3 0.33 -95.7 -98.4 118.6 0.33 -103 -102.1 127.7 0.33 -103.6 -108 188.9 5.6 48 0.27 SW 115.3 0.039 -185.4 0.33 -98 -100.7 145.7 0.33 -105.2 -104.3 144.7 0.33 -105.7 -110.2 195.2 5.0 49 0.221 SW 118.8 0.04 -185.6 0.33 -100.1 -102.9 139.3 0.33 -107.3 -106.5 144.2 0.33 -107.8 -112.4 202 6.0 50 0.298 SW 117.7 0.042 -185.6 0.33 -101.9 -104.8 119 0.33 -109.7 -108.7 148.6 0.33 -110.3 -114.9 235.4 5.1 51 0.292 SW 118.3 0.044 -185.5 0.33 -103.7 -106.7 123.7 0.33 -111.3 -110.5 115.9 0.33 -111.9 -116.8 188.7 3.4 52 0.284 SW 120.2 0.046 -185.6 0.33 -105.5 -108.6 122.4 0.33 -113.2 -112.5 141.4 0.33 -113.7 -118.7 194.7 3.7 53 0.248
140
EXP 11 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 128.9 0.052 -185.6 0.33 -107.4 -110.5 126.3 0.33 -115.5 -114.6 153.6 0.33 -116 -120.9 229.6 3.0 54 0.265 SW 134.2 0.058 -185.7 0.33 -109.1 -112.3 125 0.33 -117 -116.4 127.3 0.33 -117.3 -122.6 179.8 3.6 55 0.29 SW 131.1 0.058 -185.5 0.33 -110.9 -114.1 119.8 0.33 -119.3 -118.5 156.1 0.33 -119.8 -124.9 256.8 3.1 56 0.255 SW 131.3 0.059 -185.7 0.33 -112.5 -115.9 125.6 0.33 -120.4 -119.9 106.2 0.33 -120.7 -126.3 157.2 4.7 57 0.261 SW 124 0.059 -185.5 0.33 -114.1 -117.5 115.7 0.33 -122.5 -121.9 158.3 0.33 -122.8 -128.2 228.3 3.9 58 0.29 SW 124.1 0.062 -185.6 0.33 -115.8 -119.2 120.7 0.33 -124.1 -123.6 134.7 0.33 -124.3 -129.9 207 2.9 59 0.305 SW 120.1 0.064 -186 0.33 -117.7 -121.2 148.7 0.33 -125.9 -125.5 162.3 0.33 -125.8 -131.5 201.3 3.2 60 0.268 SW 113.9 0.066 -185.6 0.33 -119.5 -123 139.5 0.33 -127.6 -127.3 159.5 0.33 -127.5 -133.2 223.3 3.9 61 0.246 SW 111.8 0.067 -185.6 0.33 -121.6 -125.2 172.9 0.33 -129.7 -129.4 180.1 0.33 -129.5 -135.2 258.5 4.7 62 0.33 SW 108.4 0.067 -185.8 0.33 -123.2 -127 139.7 0.33 -131.2 -131.1 163.8 0.33 -130.7 -136.7 197.4 6.4 63 0.326 SW 103.9 0.069 -185.8 0.33 -124.7 -128.5 126.2 0.33 -132.7 -132.8 159.7 0.33 -132 -138 196 4.4 64 0.272 SW 104.9 0.068 -185.7 0.33 -126.5 -130.3 147.6 0.33 -134.4 -134.5 177.5 0.33 -133.6 -139.6 226 5.2 65 0.285 SW 100.7 0.069 -185.8 0.33 -127.9 -131.9 134.1 0.33 -135.8 -136 156 0.33 -134.8 -141 204.6 2.9 66 0.317 SW 101.4 0.069 -185.6 0.33 -129.2 -133.3 123.8 0.33 -136.9 -137.3 136.3 0.33 -135.9 -142.2 195.5 4.1 67 0.397 SW 100 0.069 -185.6 0.33 -130.7 -134.8 134.6 0.33 -138.6 -139 183.1 0.33 -137.5 -143.7 231.4 6.4 68 0.313 SW 99.7 0.068 -185.9 0.33 -131.3 -135.5 47.1 0.33 -139.8 -140.3 162.6 0.33 -138.6 -145 202.7 3.5 69 0.335 SW 99.1 0.068 -185.8 0.33 -134 -138 249 0.33 -141.2 -141.8 181.9 0.33 -139.6 -146.1 195.6 4.4 70 0.391 SW 99.5 0.068 -185.6 0.33 -135.2 -139.5 145.2 0.33 -142.6 -143.3 182.1 0.33 -140.9 -147.4 221.3 2.6 71 0.382 SW 96.8 0.069 -185.7 0.33 -136.7 -141 147.4 0.33 -144.3 -145 214 0.33 -142.4 -148.9 250.8 4.7 72 0.413 SW 98.7 0.067 -185.9 0.33 -137.7 -142.3 121.3 0.33 -145.3 -146.1 147.9 0.33 -143.5 -150.2 220.9 2.9 73 0.505 SW 99.6 0.067 -185.8 0.33 -139 -143.6 145 0.33 -146.2 -147.2 146.7 0.33 -144.4 -151.2 193.9 4.2 74 0.476 SW 96.3 0.068 -185.9 0.33 -140.2 -144.9 130.2 0.33 -147.6 -148.6 197.1 0.33 -145.6 -152.3 224.3 4.2 75 0.467 SW 98.9 0.066 -185.9 0.33 -141.5 -146.2 146.4 0.33 -148.9 -149.9 199.4 0.33 -146.7 -153.5 226.2 3.9 76 0.639 SW 93.7 0.067 -186.1 0.33 -142.6 -147.4 141.8 0.33 -149.8 -151 156.6 0.33 -147.6 -154.6 218 3.5 77 0.498 SW 93 0.067 -186 0.33 -144.1 -148.8 161.9 0.33 -151.3 -152.4 236.6 0.33 -148.9 -155.8 250.9 3.3 78 0.473 SW 92.4 0.067 -185.8 0.33 -145.2 -150 146.2 0.33 -152.5 -153.7 217.5 0.33 -149.9 -156.9 236.1 6.1 79 0.428 SW 89.1 0.069 -185.9 0.33 -146.2 -151 119.1 0.33 -153.7 -154.9 210.3 0.33 -151.2 -158.2 272.8 5.9 80 0.372 SW 91.5 0.068 -185.9 0.33 -147.3 -152.2 155.2 0.33 -154.6 -156 200.9 0.33 -152 -159.1 225.2 4.0 81 0.428 SW 89.2 0.069 -185.6 0.33 -148.4 -153.3 139.3 0.33 -155.7 -157.1 209 0.33 -153 -160.2 261.9 3.8 82 0.41 SW 91.5 0.068 -185.8 0.33 -149.5 -154.5 165.2 0.33 -156.8 -158.2 214.8 0.33 -154.1 -161.3 276 6.5 83 0.402 SW 88.4 0.069 -185.8 0.33 -150.4 -155.5 128.8 0.33 -157.6 -159.2 221.6 0.33 -154.7 -162.1 207 5.1 84 0.46 SW 89.1 0.068 -186.3 0.33 -151.2 -156.4 122.7 0.33 -158.3 -160 180.7 0.33 -155.3 -162.7 196.6 5.2 85 0.494 SW 90.1 0.068 -185.8 0.33 -152.1 -157.3 138.1 0.33 -159.4 -160.9 218.7 0.33 -156.5 -163.8 297 4.1 86 0.515 SW 87.7 0.068 -185.8 0.33 -152.7 -158 103 0.33 -161.2 -161.7 119.1 0.33 -160.2 -167 815.9 3.9 87 0.428 SW 90.5 0.095 -185.5 0.42 -154.3 -158.8 92.7 0.42 -171.2 -167.7 1546.8 0.17 -183 -187.8 6990.7 4.0 88 0.309 SW 92.7 0.065 -185.4 -159.9 -183.8 -189.6 5.1 89 0.298
141
EXP 12 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 59.9 1 13.1 0.33 22.2 23.2 1083.8 0.33 22.5 23.5 859.9 0.33 21.8 23.5 876.7 0.0 1 0.404 N 60 1 11.4 0.33 22.5 22.9 33.5 0.33 22.5 23.1 92.8 0.33 21.8 23 208.5 0.0 2 0.407 N 59.8 1 10.3 0.33 22 22.5 256.2 0.33 22.2 22.8 148 0.33 21.5 22.7 171.1 0.0 3 0.426 N 59.2 1 8.9 0.33 21.4 21.8 325.7 0.33 21.6 22.2 245.5 0.33 20.8 22.1 298.9 0.0 4 0.413 N 58.2 1 7.5 0.33 21.3 21.6 95.3 0.33 21.4 21.9 98.1 0.33 20.7 21.8 120.1 0.0 5 0.432 N 60.8 1 5.9 0.33 20.8 21.2 210.6 0.33 21 21.7 74.4 0.33 20.2 21.4 185.7 0.0 6 0.51 N 60.2 1 4.5 0.33 20.2 20.6 234.4 0.33 20.4 21 237 0.33 19.8 20.9 182.8 0.0 7 0.428 N 60.8 1 2.9 0.33 19.6 20 258.4 0.33 19.8 20.5 162.7 0.33 19 20.2 285.3 0.0 8 0.422 N 60.8 1 1.5 0.33 18.9 19.2 312.4 0.33 19.3 19.9 160.8 0.33 18.5 19.6 220.8 0.0 9 0.411 N 60.2 1 0.2 0.33 18.3 18.6 225.1 0.33 18.7 19.3 159.4 0.33 18 19.1 187.7 0.0 10 0.452 N 59.7 1 -1.4 0.33 17.7 17.9 243.4 0.33 18 18.7 175 0.33 17.3 18.4 238.2 0.0 11 0.428 N 61.4 1 -3.5 0.33 17 17.2 233.8 0.33 17.3 17.9 191.2 0.33 16.6 17.7 222.2 0.0 12 0.515 N 62.9 1 -5.6 0.33 16.3 16.4 238.7 0.33 16.6 17.3 134.6 0.33 15.8 16.9 228.4 0.0 13 0.431 N 62.3 1 -8.2 0.33 15.6 15.7 196.4 0.33 15.8 16.5 178.4 0.33 15.1 16.1 208.6 0.0 14 0.408 N 62.6 1 -10.4 0.33 14.8 14.9 234.4 0.33 15.2 15.9 125.1 0.33 14.4 15.4 204.4 0.0 15 0.417 N 61.1 1 -12 0.33 13.8 13.9 259.4 0.33 14.3 15 150.2 0.33 13.5 14.5 205.8 0.0 16 0.485 N 61.2 1 -15.8 0.33 12.9 12.9 211.3 0.33 13.2 14 176.2 0.33 12.4 13.4 231.1 0.0 17 0.516 N 64.2 1 -22 0.33 11.8 11.8 240.8 0.33 12.2 13 163.1 0.33 11.5 12.4 203.6 0.0 18 0.465 N 63.1 1 -23.1 0.33 10.9 10.9 207 0.33 11.2 12 144.4 0.33 10.4 11.3 238.8 0.0 19 0.403 N 63.8 1 -24 0.33 9.8 9.7 228.3 0.33 10.4 11.1 103.4 0.33 9.4 10.3 185.6 0.0 20 0.424 N 64 1 -30.2 0.33 8.7 8.6 198.9 0.33 9.1 9.9 166.6 0.33 8.3 9.2 193.2 0.0 21 0.49 N 63.2 1 -34.1 0.33 7.5 7.4 226.5 0.33 7.9 8.8 152.9 0.33 6.9 7.8 250 0.0 22 0.507 N 62.5 1 -32.7 0.33 6.2 5.9 242.3 0.33 6.7 7.6 136.9 0.33 5.7 6.5 213.6 0.0 23 0.513 N 63.9 1 -39.1 0.33 4.9 4.6 235.3 0.33 5.3 6.1 184.4 0.33 4.5 5.2 219.9 0.0 24 0.482 N 64.6 1 -38.1 0.33 3.6 3.3 171.3 0.33 4 4.9 110.3 0.33 3.1 3.7 180.7 0.0 25 0.409 N 66.7 1 -55.8 0.33 1.8 1.5 271 0.33 2.2 3.2 193 0.33 1.2 2 267.1 0.0 26 0.491 N 62.8 1 -47 0.33 0.5 0.1 205.6 0.33 1 1.8 130.5 0.33 0.2 0.7 172.2 0.0 27 0.498 N 62.9 1 -53.7 0.33 -0.9 -1.4 171.9 0.33 -0.5 0.4 120.9 0.33 -1.3 -0.8 172.2 0.0 28 0.392 N 72.1 1 -65.9 0.33 -2.4 -2.9 130.4 0.33 -2.1 -1.2 96.6 0.33 -2.9 -2.4 136 0.0 29 0.446 N 71 1 -91.2 0.33 -4.5 -4.9 147.5 0.33 -4.5 -3.2 120.9 0.33 -5.6 -5 186.2 0.0 30 0.421 N 71.8 1 -105.8 0.33 -6.8 -7.2 170.4 0.33 -7 -5.7 142.5 0.33 -8.1 -7.5 185.4 0.0 31 0.467 N 68.2 1 -106.8 0.33 -8.9 -9.4 147.1 0.33 -9.2 -7.9 114.2 0.33 -10.3 -9.9 163.9 0.0 32 0.378 N 80.2 1 -116.3 0.33 -11 -11.5 138 0.33 -11.6 -10.2 117.3 0.33 -12.9 -12.6 170.5 0.0 33 0.428 N 77 1 -124.7 0.33 -13.4 -13.9 152.1 0.33 -14.3 -12.8 132.2 0.33 -15.6 -15.4 183.2 0.0 34 0.397 N 76.7 1 -127.1 0.33 -15.7 -16.3 150.1 0.33 -16.8 -15.3 126.9 0.33 -18.2 -18.1 179.2 0.0 35 0.418 N 81.2 1 -128.1 0.33 -17.7 -18.5 132.7 0.33 -18.9 -17.5 103.9 0.33 -20.2 -20.4 149.7 0.0 36 0.396 N 78.3 1 -132.5 0.33 -20.3 -21 152.7 0.33 -21.9 -20.2 136.4 0.33 -23.5 -23.5 199.2 0.0 37 0.4 N 81.9 1 -137.5 0.33 -22.6 -23.4 119.1 0.33 -24.2 -22.7 99.7 0.33 -25.6 -26 127 0.0 38 0.401
142
EXP 12 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 86.6 1 -165.1 0.33 -24.7 -25.6 96.1 0.33 -26.7 -25.2 85.9 0.33 -28.3 -28.7 128.6 0.0 39 0.388 N 88.4 1 -185.7 0.33 -27.4 -28.2 115.1 0.33 -29.7 -28 101.5 0.33 -31.4 -31.8 146.4 0.0 40 0.39 N 85.2 1 -186 0.33 -29.8 -30.7 107.7 0.33 -32.1 -30.6 96.9 0.33 -33.6 -34.3 121.2 0.0 41 0.434 N 88.3 1 -185.3 0.33 -32 -33 101.7 0.33 -34.7 -33.1 93.3 0.33 -36.3 -37.1 136.5 0.0 42 0.441 N 89.3 1 -185.8 0.33 -34.3 -35.4 106.8 0.33 -37.1 -35.5 83 0.33 -38.9 -39.8 137.2 0.0 43 0.438 N 90.2 1 -185.3 0.33 -36.7 -37.8 110.7 0.33 -39.8 -38.2 104.9 0.33 -41.5 -42.5 139.8 0.0 44 0.433 N 88.8 1 -185.2 0.33 -39 -40.2 111.5 0.33 -42 -40.5 85.7 0.33 -43.6 -44.9 125.2 0.0 45 0.398
SW 93.1 0.039 -185.7 0.33 -41.2 -42.5 102.3 0.33 -44.5 -42.9 93.3 0.33 -46.1 -47.5 136.1 2.2 46 0.341 SW 92.3 0.039 -185.3 0.33 -43.3 -44.7 101.6 0.33 -46.9 -45.4 96 0.33 -48.6 -50.1 140.2 1.8 47 0.42 SW 94.2 0.039 -185.9 0.33 -45.6 -47 108.4 0.33 -49.4 -47.8 96.8 0.33 -51 -52.6 140.9 1.6 48 0.424 SW 94.3 0.039 -185.7 0.33 -47.4 -48.9 90.8 0.33 -51.5 -50 85.1 0.33 -53.1 -54.9 130.2 2.2 49 0.375 SW 91.4 0.039 -185.9 0.33 -49.8 -51.3 114.5 0.33 -53.8 -52.3 96.5 0.33 -55.2 -57.2 130.3 2.2 50 0.401 SW 98.8 0.038 -185.7 0.33 -51.6 -53.3 93.7 0.33 -55.9 -54.5 88.6 0.33 -57.3 -59.4 130.3 2.1 51 0.385 SW 97.8 0.038 -185.7 0.33 -53.7 -55.3 100.3 0.33 -58 -56.6 86.7 0.33 -59.5 -61.7 135.3 2.9 52 0.368 SW 105.6 0.037 -185.8 0.33 -55.7 -57.4 102 0.33 -60.2 -58.7 87.4 0.33 -61.8 -64 142.5 2.4 53 0.381 SW 98.8 0.039 -185.8 0.33 -57.6 -59.4 96 0.33 -62.4 -61 97 0.33 -63.9 -66.3 139.9 2.6 54 0.389 SW 97.3 0.039 -185.8 0.33 -59.8 -61.7 115.5 0.33 -64.4 -63.1 90.9 0.33 -65.9 -68.4 135.7 2.6 55 0.388 SW 106.5 0.038 -185.3 0.33 -61.8 -63.7 101.9 0.33 -66.7 -65.4 101.5 0.33 -68.1 -70.7 146.6 4.0 56 0.366 SW 103.5 0.038 -185.9 0.33 -63.7 -65.7 98.2 0.33 -68.8 -67.5 93.2 0.33 -70.2 -72.9 142.4 4.0 57 0.453 SW 102.2 0.039 -186.2 0.33 -65.3 -67.4 88.6 0.33 -70.5 -69.3 79.6 0.33 -72 -74.9 132.8 4.7 58 0.385 SW 102.8 0.039 -185.9 0.33 -67.2 -69.3 98.5 0.33 -72.6 -71.4 96.4 0.33 -73.9 -76.9 135.7 3.0 59 0.426 SW 100.8 0.039 -185.6 0.33 -69.2 -71.3 106.1 0.33 -74.4 -73.3 90.2 0.33 -75.6 -78.7 130.4 3.1 60 0.39 SW 108.3 0.038 -185.3 0.33 -71.2 -73.3 106.5 0.33 -76.6 -75.5 106.5 0.33 -77.8 -80.8 151 3.6 61 0.413 SW 105.7 0.039 -185.8 0.33 -73 -75.2 98.6 0.33 -78.6 -77.5 101.1 0.33 -79.7 -83 149.5 4.4 62 0.392 SW 104.5 0.039 -184.9 0.33 -74.8 -77 99.3 0.33 -80.4 -79.5 95.9 0.33 -81.3 -84.8 131.4 3.1 63 0.382 SW 103.5 0.039 -186.2 0.33 -76.5 -78.8 95.6 0.33 -82.3 -81.3 91.7 0.33 -83.2 -86.7 141.5 2.8 64 0.411 SW 104.9 0.039 -185.9 0.33 -78.3 -80.7 104.7 0.33 -83.9 -83 84.2 0.33 -84.8 -88.4 134.1 3.5 65 0.36 SW 110.8 0.039 -185.7 0.33 -80.2 -82.7 108.6 0.33 -86 -85.1 115 0.33 -86.8 -90.4 149.6 4.0 66 0.378 SW 105 0.04 -185.9 0.33 -81.6 -84.2 85.4 0.33 -87.5 -86.7 78 0.33 -88.3 -92.1 133.1 4.0 67 0.438 SW 109.1 0.039 -186.1 0.33 -83.4 -86.1 106 0.33 -89.3 -88.5 97.9 0.33 -90 -93.8 141.1 4.1 68 0.369 SW 109 0.04 -185.9 0.33 -85.1 -87.8 95.5 0.33 -91.2 -90.4 104.4 0.33 -91.8 -95.7 150.4 3.9 69 0.409 SW 109.9 0.04 -186.3 0.33 -87 -89.6 111.3 0.33 -93.2 -92.3 107.9 0.33 -93.9 -97.8 171.9 3.1 70 0.347 SW 114.3 0.04 -185.3 0.33 -88.6 -91.4 102.2 0.33 -94.7 -94.1 98.8 0.33 -95.2 -99.4 130.9 2.2 71 0.387 SW 120 0.04 -185.8 0.33 -90.1 -93 95.2 0.33 -96.4 -95.7 91.6 0.33 -96.9 -101.1 147.7 4.4 72 0.331 SW 115.5 0.041 -186.1 0.33 -91.4 -94.3 75.9 0.33 -98 -97.4 100.3 0.33 -98.5 -102.8 148.5 3.5 73 0.358 SW 124.3 0.04 -186 0.33 -93 -95.9 95.5 0.33 -99.6 -99 92.4 0.33 -100.1 -104.5 151.4 3.8 74 0.34 SW 124.6 0.041 -185.9 0.33 -94.4 -97.4 88.9 0.33 -101.1 -100.6 97.7 0.33 -101.5 -106 136.8 5.0 75 0.406 SW 118.1 0.042 -186.5 0.33 -95.7 -98.8 85.4 0.33 -102.6 -102 84.8 0.33 -103.1 -107.6 152.4 3.6 76 0.395
143
EXP 12 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 123 0.041 -185.7 0.33 -97.4 -100.5 107.3 0.33 -104.2 -103.6 101.8 0.33 -104.7 -109.3 158.5 4.4 77 0.399 SW 111.4 0.043 -185.9 0.33 -98.2 -101.5 58.3 0.33 -104.9 -104.6 53.2 0.33 -105.4 -110.3 106.4 3.1 78 0.385 SW 120.2 0.042 -186.3 0.33 -99.8 -103 93.8 0.33 -106.9 -106.4 119.7 0.33 -107.1 -111.9 156.9 1.4 79 0.357 SW 119.6 0.043 -186.5 0.33 -101.4 -104.6 108.3 0.33 -108.3 -107.8 91.5 0.33 -108.6 -113.4 155 2.3 80 0.327 SW 124.6 0.043 -186.1 0.33 -102.4 -105.8 69.6 0.33 -109.4 -109.1 81.7 0.33 -109.7 -114.7 133.3 2.5 81 0.335 SW 129.2 0.044 -186 0.33 -103.4 -106.9 70.1 0.33 -110.5 -110.2 70.7 0.33 -110.9 -116 142.4 2.9 82 0.403 SW 130.1 0.045 -186.5 0.33 -104.7 -108.1 83.8 0.33 -112 -111.6 98.7 0.33 -112.4 -117.4 157.5 3.6 83 0.349 SW 139.9 0.045 -185.8 0.33 -106 -109.5 88.8 0.33 -113.2 -112.9 84.3 0.33 -113.6 -118.7 146.6 3.8 84 0.373 SW 128.7 0.047 -186.1 0.33 -106.7 -110.4 56.7 0.33 -114 -113.8 55.1 0.33 -114.2 -119.6 112.1 3.6 85 0.359 SW 133.2 0.046 -186.5 0.33 -108.3 -111.7 95.7 0.33 -115.6 -115.3 116 0.33 -115.6 -120.9 148.7 1.8 86 0.376 SW 131.4 0.047 -186.1 0.33 -109.1 -112.8 66.1 0.33 -116.4 -116.2 60.6 0.33 -116.6 -122 137.8 3.3 87 0.317 SW 127.3 0.047 -185.9 0.33 -110.1 -113.7 66.9 0.33 -117.5 -117.3 75.5 0.33 -117.7 -123.2 146.9 2.8 88 0.295 SW 133.4 0.048 -186.2 0.33 -111.4 -115 88.4 0.33 -118.8 -118.6 95.4 0.33 -118.8 -124.3 146.6 2.1 89 0.328 SW 137.2 0.048 -186.1 0.33 -112.1 -115.9 62.2 0.33 -119.6 -119.5 69.2 0.33 -119.7 -125.3 129.7 3.0 90 0.331 SW 132.3 0.05 -186.1 0.33 -113.2 -116.9 65.5 0.33 -121 -120.7 93.8 0.33 -121.1 -126.7 171.6 5.8 91 0.32 SW 146.7 0.052 -186.1 0.33 -114.5 -118.2 97.2 0.33 -122.1 -121.9 85.7 0.33 -122.2 -127.9 158.6 3.1 92 0.36 SW 147.7 0.052 -186.2 0.33 -114.9 -118.9 40.3 0.33 -122.9 -122.7 60 0.33 -123.1 -128.9 139.3 2.9 93 0.328 SW 140.7 0.052 -186.2 0.33 -116 -119.8 68.6 0.33 -124.1 -123.8 90.2 0.33 -124.3 -130 162.5 3.4 94 0.331 SW 137.6 0.053 -186 0.33 -117.2 -121 90.8 0.33 -124.9 -124.9 82.3 0.33 -124.9 -130.9 128.9 2.7 95 0.356 SW 145.9 0.053 -186.3 0.33 -117.7 -121.7 40.6 0.33 -125.8 -125.8 71.9 0.33 -125.9 -131.8 146.6 2.9 96 0.343 SW 145.3 0.055 -186.2 0.33 -119.1 -122.9 95.1 0.33 -127.1 -126.9 95.9 0.33 -127.2 -133 178 3.5 97 0.339 SW 143.2 0.057 -186.1 0.33 -119.4 -123.5 35.1 0.33 -127.6 -127.6 51.1 0.33 -127.6 -133.8 122.7 6.7 98 0.334 SW 142.1 0.06 -186.2 0.33 -120.9 -124.7 97.4 0.33 -129 -128.9 119.7 0.33 -129 -134.9 179.9 3.1 99 0.336 SW 152.5 0.064 -186 0.33 -121.1 -125.3 34.8 0.33 -129.1 -129.3 24.8 0.33 -129.1 -135.4 100.2 2.6 100 0.317 SW 151.7 0.063 -186.7 0.33 -122.3 -126.3 80.3 0.33 -130.6 -130.5 110.5 0.33 -130.6 -136.7 193.5 3.2 101 0.342 SW 137.3 0.06 -186.5 0.33 -122.9 -127.1 56.4 0.33 -131 -131.1 50.7 0.33 -130.9 -137.2 112 3.2 102 0.267 SW 135.9 0.061 -185.7 0.33 -124.1 -128.2 88.9 0.33 -132.2 -132.3 118.6 0.33 -131.7 -137.9 141.1 2.6 103 0.299 SW 144.4 0.063 -186 0.33 -124.7 -128.9 52.6 0.33 -132.9 -133 53.9 0.33 -132.7 -139 172 3.1 104 0.36 SW 169.9 0.068 -186.4 0.33 -125.5 -129.7 65.7 0.33 -133.4 -133.7 72.6 0.33 -133 -139.5 110.4 1.9 105 0.352 SW 154.8 0.073 -186.7 0.33 -126 -130.3 42.7 0.33 -134.3 -134.4 65.5 0.33 -134 -140.4 167.9 7.5 106 0.284 SW 138.5 0.073 -186.3 0.33 -127.4 -131.5 100.9 0.33 -135.6 -135.8 140 0.33 -135.1 -141.4 180.3 4.1 107 0.316 SW 148.9 0.078 -185.9 0.33 -127.5 -132 26.8 0.33 -135.5 -136.1 25.1 0.33 -134.8 -141.5 66.7 2.4 108 0.321 SW 163.9 0.079 -186.4 0.33 -128.5 -132.8 70.7 0.33 -136.6 -136.9 99.8 0.33 -136 -142.4 169.1 3.6 109 0.338 SW 158.3 0.078 -186.5 0.33 -129.7 -133.9 101.6 0.33 -137.8 -138 115.8 0.33 -137.1 -143.5 194.8 3.1 110 0.313 SW 151.2 0.076 -186.3 0.33 -129.8 -134.3 13.7 0.33 -137.9 -138.5 46.8 0.33 -137.2 -143.9 98.9 4.0 111 0.299 SW 144.9 0.077 -186 0.33 -130.9 -135.2 86.4 0.33 -139.1 -139.5 113.1 0.33 -138.4 -144.9 194 1.9 112 0.313 SW 157.9 0.081 -186.2 0.33 -131.7 -136.1 75 0.33 -139.7 -140.2 78.8 0.33 -138.9 -145.6 146.9 3.2 113 0.368 SW 176.4 0.084 -186.3 0.33 -132 -136.5 28.9 0.33 -140.2 -140.8 75.8 0.33 -139.2 -146 111.3 3.0 114 0.337
144
EXP 12 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 148.3 0.079 -186.7 0.33 -133.4 -137.8 125.3 0.33 -141.1 -141.6 88.8 0.33 -140.3 -146.9 186.9 6.0 115 0.322 SW 139.1 0.08 -186 0.33 -133.8 -138.4 49 0.33 -141.7 -142.4 93 0.33 -140.6 -147.4 120.5 3.6 116 0.303 SW 157.4 0.085 -186.4 0.33 -134.3 -138.9 38.7 0.33 -142.2 -142.9 66.6 0.33 -141.1 -147.9 139.9 3.3 117 0.375 SW 164.3 0.085 -186.3 0.33 -135.5 -140 110.7 0.33 -143.2 -143.8 117.2 0.33 -142.1 -148.8 181.2 4.7 118 0.352 SW 141 0.084 -186.7 0.33 -135.9 -140.6 47.8 0.33 -143.9 -144.5 86.2 0.33 -142.7 -149.5 168.9 6.0 119 0.308 SW 143.7 0.088 -186.3 0.33 -137 -141.6 109.2 0.33 -144.7 -145.4 105.6 0.33 -143.5 -150.3 172.4 3.6 120 0.314 SW 146.4 0.089 -186.1 0.33 -137.1 -142 23.1 0.33 -145.2 -145.9 61.3 0.33 -144.2 -151.1 174 3.2 121 0.376 SW 158.1 0.088 -186.1 0.33 -138.6 -143.3 141.9 0.33 -146.1 -146.9 141.6 0.33 -144.7 -151.6 148.2 2.2 122 0.307 SW 147.4 0.089 -186.6 0.33 -138.9 -143.7 33.8 0.33 -146.9 -147.8 125.8 0.33 -145.3 -152.2 160.5 2.5 123 0.314 SW 146.2 0.088 -186.1 0.33 -139.2 -144.2 41.9 0.33 -146.9 -147.9 24.8 0.33 -145.4 -152.5 113.4 3.4 124 0.374 SW 135.9 0.083 -186.3 0.33 -140.4 -145.2 116.8 0.33 -147.8 -148.8 133.1 0.33 -146.1 -153.1 162.8 1.9 125 0.354 SW 134.8 0.086 -186.1 0.33 -140.8 -145.8 52.2 0.33 -148.2 -149.3 78.3 0.33 -146.4 -153.5 118.2 2.1 126 0.339 SW 135.1 0.083 -186.4 0.33 -141.6 -146.5 85.4 0.33 -148.9 -150 109.3 0.33 -147 -154 154.8 3.3 127 0.39 SW 130.8 0.079 -186.6 0.33 -143 -147.8 159.9 0.33 -150.1 -151.1 151.1 0.33 -148.3 -155.2 244.5 3.3 128 0.331 SW 129.4 0.08 -186.5 0.33 -143 -148.1 14.6 0.33 -150.5 -151.7 104.2 0.33 -148.6 -155.8 152.7 4.0 129 0.34 SW 135.5 0.081 -186.5 0.33 -143.4 -148.6 51.4 0.33 -150.5 -152 60.2 0.33 -148.4 -155.7 60.4 1.9 130 0.381 SW 126.7 0.083 -186.7 0.33 -144.7 -149.6 137.5 0.33 -151.6 -152.9 164.2 0.33 -149.2 -156.3 169.1 3.1 131 0.349 SW 136 0.09 -186.6 0.33 -145.3 -150.4 86.7 0.33 -152.6 -153.7 115.5 0.33 -150.7 -157.7 297.6 4.3 132 0.322 SW 137.4 0.091 -186.4 0.33 -145.2 -150.6 11.7 0.33 -152.4 -153.9 53.9 0.33 -150.2 -157.7 51.2 2.0 133 0.338 SW 138 0.093 -186.2 0.33 -146.8 -151.7 160.3 0.33 -154.3 -155.2 220.1 0.33 -152.2 -159.2 344.9 3.9 134 0.284 SW 143.1 0.09 -186.6 0.33 -146.5 -151.9 3.2 0.33 -154.4 -155.6 70.2 0.33 -153.9 -161.1 492.2 5.1 135 0.297 SW 145 0.089 -186.3 0.42 -147.9 -152.6 88.4 0.42 -161.6 -159.1 694.5 0.17 -174.7 -179.5 4661.5 4.0 136 0.275 SW 131.3 0.091 -185.9 0.42 -153.6 -153.7 49.7 0.42 -180.4 -173.7 2917 0.17 -179.4 -184.2 6111.1 3.5 137 0.282 SW 145.6 0.089 -186.7 -154.4 -181 -185.4 4.7 138 0.32 SW 135.6 0.091 -186.4 -156.2 -183.1 -185.9 2.5 139 0.218 SW 137 0.092 -186.1 -158.3 -183.6 -185.3 3.4 140 0.326 SW 147.6 0.09 -186.2 -161.7 -185.2 -186.1 2.8 141 0.25 SW 139.7 0.093 -186.2 -163.9 -185.6 -186.2 2.3 142 0.308 SW 147.1 0.09 -186.3 -167 -185.5 -185.8 5.5 143 0.301
EXP 13 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 59.1 1 9.9 0.33 22.2 23.2 770.2 0.33 22.6 23.6 557.1 0.33 21.9 23.5 677.3 0.0 1 0.311 N 58.9 1 7.7 0.33 22.2 22.7 325.9 0.33 22.2 22.9 228.8 0.33 21.5 22.8 264.1 0.0 2 0.332 N 59.1 1 5.7 0.33 21.3 21.9 302.6 0.33 21.6 22.4 252.5 0.33 20.7 22 305 0.0 3 0.308 N 59.9 1 2.9 0.33 20.6 21 302.4 0.33 21 21.6 172.8 0.33 20.3 21.5 158.8 0.0 4 0.327
145
EXP 13 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 60.2 1 0.7 0.33 19.9 20.3 356 0.33 20.2 21 316.1 0.33 19.4 20.6 277.2 0.0 5 0.32 N 61.6 1 -2.3 0.33 18.8 19.3 304.7 0.33 19.1 20 248.4 0.33 18.3 19.6 297.5 0.0 6 0.279 N 61.1 1 -6 0.33 17.9 18.3 324 0.33 18.2 19 207.5 0.33 17.4 18.7 242.3 0.0 7 0.3 N 63.1 1 -8.9 0.33 16.9 17.2 361.8 0.33 17.1 18 276.7 0.33 16.3 17.5 249.4 0.0 8 0.338 N 63.3 1 -15.6 0.33 15.4 15.7 268.4 0.33 16 16.9 218.2 0.33 15.1 16.3 269.4 0.0 9 0.288 N 61.7 1 -16.1 0.33 14 14.3 272.3 0.33 14.5 15.5 250.3 0.33 13.6 14.9 321.5 0.0 10 0.392 N 63.2 1 -18.1 0.33 13 13.1 247.2 0.33 13.4 14.3 165.4 0.33 12.5 13.6 255.3 0.0 11 0.31 N 60.7 1 -22.8 0.33 11.8 11.8 193.7 0.33 12.1 13 184.4 0.33 11.2 12.2 238.6 0.0 12 0.358 N 63.4 1 -27.7 0.33 10.1 10.2 253.9 0.33 10.6 11.6 222.6 0.33 9.7 10.7 210.7 0.0 13 0.308 N 64.7 1 -42.5 0.33 8.5 8.5 188.4 0.33 8.7 9.9 155.7 0.33 7.6 8.7 221.5 0.0 14 0.335
SW 64 1 -58.7 0.33 6.2 6.3 209.1 0.33 6.5 7.8 187.7 0.33 5.2 6.4 243 1.4 15 0.343 N 66.8 1 -64.1 0.33 4.5 4.5 312.4 0.33 4.5 5.8 277.9 0.33 3.3 4.3 204.6 0.0 16 0.339
SW 67.7 0.043 -69.5 0.33 1.8 1.8 191.7 0.33 2.1 3.5 125.4 0.33 0.9 1.8 217.3 1.9 17 0.254 N 66.7 0.044 -79.4 0.33 -0.5 -0.6 172.1 0.33 -0.5 1 177.2 0.33 -1.7 -0.8 236.6 0.0 18 0.322
SW 66.1 0.044 -82 0.33 -2.8 -3 222.1 0.33 -2.7 -1.4 186.9 0.33 -3.8 -3.2 189.2 1.5 19 0.324 SW 71.6 0.041 -93 0.33 -5.1 -5.3 172.4 0.33 -5.3 -3.9 157.9 0.33 -6.5 -5.8 204.2 2.2 20 0.3 SW 68.4 0.043 -100.4 0.33 -7.6 -7.9 194.6 0.33 -7.8 -6.4 176.4 0.33 -8.9 -8.4 158.5 2.0 21 0.322 N 76.4 0.04 -126 0.33 -10.7 -10.8 129.9 0.33 -11.5 -9.7 108.7 0.33 -12.8 -12.1 216.7 0.0 22 0.288
SW 80.6 0.039 -135 0.33 -13.7 -14 138.8 0.33 -14.9 -13 139.2 0.33 -16.4 -15.9 167.1 2.3 23 0.285 N 82.1 0.038 -177.7 0.33 -16.7 -17.1 150.1 0.33 -18.3 -16.3 133.3 0.33 -19.9 -19.6 159.3 0.0 24 0.289
SW 90.9 0.036 -185.1 0.33 -19.8 -20.1 139.2 0.33 -21.8 -19.7 125.5 0.33 -23.8 -23.5 173.7 2.6 25 0.255 SW 92.8 0.036 -185.8 0.33 -22.6 -23.1 128.6 0.33 -25 -22.8 115.2 0.33 -27.2 -27.2 166.9 2.2 26 0.293 SW 92.6 0.036 -185.3 0.33 -25.6 -26.1 134.6 0.33 -28.4 -26.2 130.4 0.33 -30.6 -30.8 166.9 3.0 27 0.262 SW 92.8 0.037 -185.1 0.33 -28.5 -29.1 139.2 0.33 -31.7 -29.4 121.1 0.33 -33.9 -34.3 170.7 3.5 28 0.235 SW 92.6 0.037 -184.6 0.33 -32.6 -33 150.5 0.33 -35.9 -33.4 131.5 0.33 -38.2 -38.6 206.8 2.9 29 0.241 SW 93.9 0.037 -185.6 0.33 -35.2 -36 136.1 0.33 -38.8 -36.6 124.6 0.33 -41.1 -41.9 166.8 4.2 30 0.235 SW 95.2 0.037 -184.9 0.33 -38.3 -39.1 144 0.33 -42.2 -39.9 121.1 0.33 -44.3 -45.3 173 3.8 31 0.256 SW 98.2 0.036 -185.5 0.33 -40.8 -41.8 145.9 0.33 -44.9 -42.8 139.4 0.33 -47.2 -48.4 164.3 4.2 32 0.26 SW 95 0.037 -185.5 0.33 -43.7 -44.7 120.1 0.33 -48 -45.9 116.6 0.33 -50 -51.4 166.1 3.1 33 0.256 SW 100.1 0.036 -185 0.33 -46.5 -47.5 177.4 0.33 -51 -49 159.8 0.33 -53.1 -54.6 176 3.5 34 0.26 SW 101.3 0.037 -185.4 0.33 -49 -50.2 144.6 0.33 -53.7 -51.7 112.7 0.33 -56 -57.7 172.5 2.4 35 0.293 SW 104.4 0.036 -185.3 0.33 -51.5 -52.8 124.9 0.33 -56.4 -54.4 112.1 0.33 -58.4 -60.4 158 4.0 36 0.273 SW 104.7 0.037 -185.7 0.33 -54.4 -55.7 134.4 0.33 -59.2 -57.4 111.8 0.33 -61 -63.1 160.8 3.3 37 0.275 SW 104 0.037 -185.3 0.33 -56.7 -58.1 146 0.33 -62 -60.2 125.8 0.33 -63.8 -66 174.4 4.1 38 0.292 SW 105.9 0.037 -185.5 0.33 -59.2 -60.7 124.9 0.33 -64.4 -62.8 137.9 0.33 -66.1 -68.5 158 2.5 39 0.281 SW 106.8 0.037 -185.4 0.33 -61.4 -63 130.1 0.33 -67.2 -65.4 89.7 0.33 -69 -71.4 182.8 4.4 40 0.263 SW 106.6 0.038 -185.5 0.33 -63.9 -65.5 129.5 0.33 -69.6 -68 122 0.33 -71.2 -73.9 158.4 3.9 41 0.234 SW 107.6 0.038 -185.5 0.33 -66.5 -68.1 130 0.33 -72.2 -70.6 123.1 0.33 -73.7 -76.5 170.3 4.6 42 0.269
146
EXP 13 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 108.4 0.038 -185.5 0.33 -68.8 -70.6 142.9 0.33 -74.7 -73.1 120.5 0.33 -76.2 -79.1 174.8 3.9 43 0.26 SW 109 0.038 -185.5 0.33 -70.9 -72.8 122.2 0.33 -77 -75.5 120.5 0.33 -78.5 -81.5 168.5 3.8 44 0.3 SW 111.2 0.038 -185.6 0.33 -73.2 -75.2 119.1 0.33 -79.5 -78 112.4 0.33 -81 -84.2 182.2 4.8 45 0.251 SW 114.6 0.038 -185.5 0.33 -75.5 -77.5 129.3 0.33 -81.8 -80.4 107.7 0.33 -83.1 -86.4 162.8 3.8 46 0.242 SW 118.1 0.039 -185.7 0.33 -77.4 -79.6 115.3 0.33 -83.9 -82.5 98.9 0.33 -85.4 -88.8 175.1 3.3 47 0.254 SW 117 0.04 -185.8 0.33 -79.3 -81.5 134 0.33 -86.2 -84.8 131.1 0.33 -87.6 -91.1 175.8 3.2 48 0.248 SW 124.7 0.04 -185.8 0.33 -81.4 -83.6 137.8 0.33 -88.5 -87.1 108.7 0.33 -89.8 -93.5 181.6 4.0 49 0.253 SW 123.9 0.041 -185.1 0.33 -83.5 -85.8 92.1 0.33 -90.7 -89.3 103.8 0.33 -92.1 -95.9 186.2 3.8 50 0.254 SW 129.1 0.042 -185.7 0.33 -85.1 -87.5 121.9 0.33 -92.6 -91.2 81.5 0.33 -94.1 -98 175.9 3.6 51 0.276 SW 128.8 0.042 -185.6 0.33 -86.9 -89.4 131.4 0.33 -94.3 -93 117.9 0.33 -95.7 -99.8 157.1 4.1 52 0.24 SW 130.1 0.042 -185.7 0.33 -88.7 -91.2 116.8 0.33 -96.3 -95.1 109.3 0.33 -97.6 -101.8 172.8 3.4 53 0.311 SW 131.3 0.043 -185.6 0.33 -90.4 -93 126.3 0.33 -98.1 -96.9 111.4 0.33 -99.6 -103.9 182.1 4.1 54 0.274 SW 126.4 0.044 -185 0.33 -92.3 -94.8 112.1 0.33 -100.1 -98.9 119.4 0.33 -101.5 -105.9 182.6 4.7 55 0.251 SW 129.1 0.045 -185.6 0.33 -93.7 -96.4 106.4 0.33 -101.8 -100.6 84.6 0.33 -103.2 -107.7 170.6 3.5 56 0.268 SW 132.4 0.046 -185.6 0.33 -95.4 -98.2 110 0.33 -103.5 -102.4 113.6 0.33 -104.7 -109.3 161.7 2.5 57 0.259 SW 132.6 0.047 -185.3 0.33 -97.1 -99.9 121.8 0.33 -105.1 -104.1 88.1 0.33 -106.4 -111.1 172.8 2.9 58 0.307 SW 137.6 0.048 -186.1 0.33 -98.7 -101.6 114 0.33 -106.7 -105.7 90.2 0.33 -107.9 -112.7 167.3 5.6 59 0.287 SW 133.2 0.049 -185.6 0.33 -100.4 -103.3 120.3 0.33 -108.4 -107.5 112.2 0.33 -109.5 -114.3 173.3 2.6 60 0.342 SW 135.3 0.049 -185.6 0.33 -102 -105 122.7 0.33 -110 -109.2 110.3 0.33 -110.9 -115.9 166.1 2.2 61 0.385 SW 138.8 0.05 -185.8 0.33 -103.1 -106.3 120.3 0.33 -111.2 -110.5 105.6 0.33 -112.1 -117.2 151.2 1.8 62 0.246 SW 135.4 0.05 -185.4 0.33 -104.9 -108 88.4 0.33 -113 -112.1 66.1 0.33 -113.9 -119 193 4.0 63 0.316 SW 138.6 0.049 -185.5 0.33 -106.3 -109.5 133.8 0.33 -114.4 -113.7 119 0.33 -115.3 -120.5 177.2 2.5 64 0.403 SW 132.2 0.051 -185.5 0.33 -107.6 -110.8 101.3 0.33 -115.9 -115.2 86.5 0.33 -116.5 -121.8 157.4 4.7 65 0.302 SW 139.6 0.052 -185.5 0.33 -109.3 -112.6 130.5 0.33 -117.2 -116.7 140.2 0.33 -117.7 -123.1 162.5 6.0 66 0.358 SW 138.3 0.054 -185.6 0.33 -110.5 -113.8 91.7 0.33 -118.9 -118.2 65.2 0.33 -119.5 -124.9 204.7 3.0 67 0.325 SW 137.7 0.056 -185.2 0.33 -111.9 -115.3 153.8 0.33 -119.9 -119.5 103.4 0.33 -120.3 -126 143.1 4.1 68 0.382 SW 137.1 0.057 -185.8 0.33 -113.2 -116.7 76.2 0.33 -121.3 -120.9 109 0.33 -121.6 -127.2 169.8 7.7 69 0.39 SW 141.9 0.059 -185.8 0.33 -114.3 -117.9 89.3 0.33 -122.2 -122 64.8 0.33 -122.5 -128.3 148.3 3.0 70 0.385 SW 130.2 0.059 -185.4 0.33 -116 -119.5 129 0.33 -123.9 -123.6 114.5 0.33 -123.8 -129.5 164.9 2.4 71 0.389 SW 133.3 0.06 -185.8 0.33 -116.9 -120.6 90.7 0.33 -124.8 -124.7 98 0.33 -124.8 -130.6 156.2 2.7 72 0.375 SW 136.3 0.063 -185.5 0.33 -118.4 -122.1 111.8 0.33 -126.3 -126.1 68.9 0.33 -126.2 -131.9 184 2.5 73 0.318 SW 132.1 0.064 -185.8 0.33 -119.5 -123.4 157 0.33 -127.3 -127.3 164.3 0.33 -126.9 -132.9 144.6 3.6 74 0.454 SW 129.9 0.065 -185.7 0.33 -120.8 -124.7 120.1 0.33 -128.6 -128.6 101.5 0.33 -128.2 -134.1 178.7 2.1 75 0.405 SW 132 0.065 -185.7 0.33 -121.8 -125.8 142.9 0.33 -129.5 -129.7 132.6 0.33 -129 -135.1 148.5 3.2 76 0.516 SW 134.6 0.066 -186 0.33 -123 -127 73.6 0.33 -130.8 -131 80.1 0.33 -130.2 -136.2 168 2.8 77 0.477 SW 128.6 0.066 -185.7 0.33 -124.3 -128.3 142.8 0.33 -131.8 -132.1 100.5 0.33 -131.1 -137.3 161.6 4.1 78 0.531 SW 126.6 0.066 -185.9 0.33 -125.5 -129.6 119.5 0.33 -133 -133.3 99.1 0.33 -132.2 -138.4 171.9 3.1 79 0.326 SW 130.5 0.067 -186 0.33 -126.5 -130.7 99.3 0.33 -134 -134.4 28 0.33 -133.1 -139.4 165.1 4.6 80 0.46
147
EXP 13 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 130.5 0.068 -185.6 0.33 -127.9 -132 78.3 0.33 -135.5 -135.9 131.1 0.33 -134.4 -140.6 196 3.0 81 0.462 SW 132 0.07 -185 0.33 -129.1 -133.4 158.4 0.33 -136.2 -136.8 159.5 0.33 -135 -141.4 141.7 3.1 82 0.361 SW 132.7 0.071 -185.8 0.33 -130.2 -134.6 124.1 0.33 -137.3 -138 124.8 0.33 -135.8 -142.3 147.9 1.7 83 0.467 SW 132.6 0.074 -186 0.33 -130.9 -135.5 176.7 0.33 -138.1 -138.8 130.2 0.33 -136.8 -143.2 168 3.1 84 0.42 SW 143.3 0.084 -185.7 0.33 -132.1 -136.5 100.1 0.33 -139.4 -140 105.4 0.33 -138.1 -144.4 201.6 6.7 85 0.474 SW 141.5 0.088 -185.8 0.33 -133.3 -137.8 124.7 0.33 -140.4 -141.1 81 0.33 -138.9 -145.4 175.9 3.3 86 0.483 SW 141.1 0.089 -185.8 0.33 -134.1 -138.7 66.7 0.33 -141.1 -141.9 27.1 0.33 -139.7 -146.3 161.5 3.5 87 0.505 SW 141 0.091 -185.5 0.33 -135.4 -139.9 157.4 0.33 -142.4 -143.3 230.5 0.33 -140.7 -147.3 183.3 3.3 88 0.442 SW 139.3 0.092 -185.8 0.33 -136.3 -141 120.8 0.33 -143.4 -144.3 31.1 0.33 -141.5 -148.2 174 2.8 89 0.479 SW 135.9 0.092 -185.6 0.33 -137.2 -141.9 75.2 0.33 -144.3 -145.3 140.4 0.33 -142.5 -149.2 189.5 7.2 90 0.403 SW 134.6 0.093 -185.9 0.33 -137.8 -142.7 185.5 0.33 -144.8 -145.8 62.5 0.33 -143.2 -150 167 3.9 91 0.335 SW 135.8 0.093 -185.9 0.33 -138.9 -143.8 42.2 0.33 -145.8 -146.8 8.4 0.33 -144 -150.8 174.3 3.5 92 0.406 SW 133.8 0.092 -185.5 0.33 -139.8 -144.7 126.7 0.33 -146.9 -147.9 242.9 0.33 -145 -151.8 206.2 3.1 93 0.467 SW 132.4 0.093 -185.6 0.33 -140.7 -145.7 202.8 0.33 -147.8 -148.8 66.2 0.33 -145.9 -152.8 205.1 4.2 94 0.49 SW 133.8 0.093 -185.8 0.33 -141.6 -146.6 50 0.33 -148.3 -149.6 61.1 0.33 -146.3 -153.3 137.1 3.3 95 0.471 SW 136.3 0.092 -185.8 0.33 -142.2 -147.3 76.3 0.33 -149.2 -150.5 138.3 0.33 -147 -154 169.4 2.9 96 0.41 SW 133.7 0.092 -185.8 0.33 -143.2 -148.2 221 0.33 -150.1 -151.3 220.7 0.33 -148.1 -155 225.6 3.8 97 0.407 SW 133.8 0.092 -185.5 0.33 -143.9 -149 153.1 0.33 -151 -152.3 64.4 0.33 -148.6 -155.7 169.5 4.3 98 0.543 SW 131.9 0.091 -185.5 0.33 -144.6 -149.8 48.4 0.33 -151.3 -152.8 38.3 0.33 -148.9 -156.1 126.4 3.6 99 0.525 SW 130.8 0.09 -185.5 0.33 -145.7 -150.9 196.1 0.33 -152.3 -153.6 279.3 0.33 -150 -157.1 237 2.8 100 0.387 SW 132.3 0.089 -185.7 0.33 -146.2 -151.4 179.9 0.33 -153.1 -154.5 53.3 0.33 -150.7 -157.8 189.2 4.2 101 0.498 SW 126.6 0.087 -185.8 0.33 -147.1 -152.3 106.9 0.33 -153.8 -155.2 32.1 0.33 -151.3 -158.6 190.1 2.8 102 0.505 SW 112.5 0.08 -186.1 0.33 -147.7 -153.1 55.8 0.33 -154.1 -155.8 214.9 0.33 -151.3 -158.7 97.8 3.5 103 0.507 SW 123.7 0.089 -185.9 0.33 -148.4 -153.7 252.8 0.33 -155.3 -156.8 97 0.33 -152.6 -159.8 265.2 3.4 104 0.438 SW 129.4 0.091 -185.7 0.33 -149.6 -154.8 82.2 0.33 -156 -157.6 66.6 0.33 -153.3 -160.6 206.8 3.1 105 0.358 SW 130.9 0.038 -186 0.42 -150.1 -155.5 166.8 0.42 -158.9 -158.4 1254.8 0.17 -169.6 -175.2 3724.1 2.7 106 0.327 SW 123.5 0.038 -185.6 0.42 -152 -156 13.5 0.42 -171.3 -167.7 4871.3 0.17 -177.6 -183.2 6916.5 2.6 107 0.274 SW 130.2 0.091 -185.4 -157.2 -180 -184.8 2.6 108 0.321 SW 128.3 0.092 -185.7 -158.8 -183.2 -184.8 4.8 109 0.533 SW 129.3 0.092 -185.6 -162.4 -185 -185.5 4.7 110 0.465 SW 125.9 0.094 -185.8 -166.4 -185.3 -185.8 4.8 111 0.318
EXP 14 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 59.4 1 10.5 0.33 21.8 22.7 770.2 0.33 22.4 23.1 557.1 0.33 22 23.4 394.5 0.0 1 0.339 N 60.2 1 8 0.33 21.4 21.9 325.9 0.33 21.8 22.4 228.8 0.33 21.2 22.6 363.5 0.0 2 0.345
148
EXP 14 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 60.2 1 6 0.33 20.7 21.1 302.6 0.33 21.2 21.7 252.5 0.33 20.7 21.9 217.1 0.0 3 0.331 N 60.9 1 3.3 0.33 19.9 20.3 302.4 0.33 20.4 21.1 172.8 0.33 19.8 21.1 294.3 0.0 4 0.346 N 61.5 1 0 0.33 18.7 19.2 356 0.33 19.3 20 316.1 0.33 18.8 20.1 287.9 0.0 5 0.352 N 62.2 1 -3.4 0.33 17.8 18.2 304.7 0.33 18.4 19 248.4 0.33 17.9 19.2 237.3 0.0 6 0.338 N 62.2 1 -7.1 0.33 16.6 17 324 0.33 17.3 18 207.5 0.33 16.7 18 306.2 0.0 7 0.325 N 61.8 1 -10.4 0.33 15.2 15.5 361.8 0.33 16 16.7 276.7 0.33 15.6 16.8 252.5 0.0 8 0.385 N 62.2 1 -14.2 0.33 14 14.2 268.4 0.33 14.7 15.4 218.2 0.33 14.2 15.4 280.7 0.0 9 0.385 N 65.8 1 -19.9 0.33 12.5 12.8 272.3 0.33 13.1 13.9 250.3 0.33 12.8 14 245 0.0 10 0.348 N 63.7 1 -27.5 0.33 10.8 11 247.2 0.33 11.6 12.4 165.4 0.33 11.2 12.3 215.3 0.0 11 0.328 N 63.9 1 -41.4 0.33 8.8 9.1 193.7 0.33 9.4 10.4 184.4 0.33 8.9 10.2 208.2 0.0 12 0.357 N 68.5 1 -63.6 0.33 6.6 6.9 253.9 0.33 7.2 8.1 222.6 0.33 6.9 8 230.3 0.0 13 0.388 N 65.6 0.489 -56.6 0.33 4.7 4.8 188.4 0.33 5.1 6.1 155.7 0.33 4.5 5.7 208.4 0.0 14 0.283 N 67.2 0.301 -74.4 0.33 2.1 2.3 209.1 0.33 2.4 3.6 187.7 0.33 1.9 3 215.8 0.0 15 0.395 N 69 0.215 -84.1 0.33 -0.7 -0.5 312.4 0.33 -0.5 0.7 277.9 0.33 -0.9 0.2 301.9 0.0 16 0.353 N 66 0.175 -65 0.33 -2.9 -3.1 191.7 0.33 -2.6 -1.4 125.4 0.33 -3.5 -2.6 210.4 0.0 17 0.306 N 73.7 0.134 -95.8 0.33 -5.4 -5.5 172.1 0.33 -5.4 -4.2 177.2 0.33 -5.8 -5.1 169.3 0.0 18 0.303
SW 72.5 0.029 -107.3 0.33 -8.7 -8.7 222.1 0.33 -8.8 -7.3 186.9 0.33 -9.4 -8.6 236.6 3.3 19 0.346 SW 75.2 0.028 -111.6 0.33 -11.3 -11.6 172.4 0.33 -11.7 -10.3 157.9 0.33 -12.5 -11.9 202.9 1.8 20 0.326 SW 78.1 0.027 -125.8 0.33 -14.7 -14.8 194.6 0.33 -15.2 -13.7 176.4 0.33 -15.9 -15.4 207.5 2.5 21 0.296 SW 79.2 0.027 -133.8 0.33 -17.6 -18 129.9 0.33 -18.3 -16.8 108.7 0.33 -19.3 -18.9 149.9 2.5 22 0.285 SW 93.9 0.025 -184.3 0.33 -20.9 -21.2 138.8 0.33 -22.3 -20.5 139.2 0.33 -23.4 -23.1 178.9 3.1 23 0.304 SW 95.4 0.025 -184.8 0.33 -24.3 -24.8 150.1 0.33 -25.9 -24.1 133.3 0.33 -27.1 -27 171.9 3.7 24 0.317 SW 94.3 0.025 -185.3 0.33 -27.4 -28 139.2 0.33 -29.4 -27.5 125.5 0.33 -30.8 -30.9 177.7 3.7 25 0.308 SW 95.4 0.025 -185.3 0.33 -30.2 -31 128.6 0.33 -32.6 -30.7 115.2 0.33 -34.3 -34.7 173.2 4.3 26 0.295 SW 96.4 0.025 -185.3 0.33 -33.2 -34 134.6 0.33 -36.1 -34.1 130.4 0.33 -37.8 -38.3 174.8 3.1 27 0.284 SW 96.4 0.026 -185.3 0.33 -36.2 -37.1 139.2 0.33 -39 -37.2 121.1 0.33 -40.5 -41.4 151.6 3.1 28 0.264 SW 95.9 0.026 -185.5 0.33 -39.5 -40.4 150.5 0.33 -42.5 -40.6 131.5 0.33 -44.1 -45 183 2.4 29 0.267 SW 97.4 0.026 -185.1 0.33 -42.3 -43.4 136.1 0.33 -45.5 -43.7 124.6 0.33 -47.2 -48.3 170 2.6 30 0.249 SW 96.7 0.026 -185.2 0.33 -45.2 -46.4 144 0.33 -48.5 -46.7 121.1 0.33 -50 -51.4 161.4 3.7 31 0.281 SW 100.2 0.026 -185.7 0.33 -48.3 -49.5 145.9 0.33 -51.9 -50.1 139.4 0.33 -53.3 -54.7 182.2 3.5 32 0.275 SW 101.6 0.026 -185.7 0.33 -50.6 -52.1 120.1 0.33 -54.6 -52.9 116.6 0.33 -56.1 -57.8 167.6 3.5 33 0.268 SW 107 0.026 -185.4 0.33 -54.4 -55.6 177.4 0.33 -58.5 -56.5 159.8 0.33 -60 -61.6 212.9 4.1 34 0.287 SW 105.9 0.026 -185.3 0.33 -56.9 -58.6 144.6 0.33 -60.8 -59.3 112.7 0.33 -62.3 -64.4 159.9 3.3 35 0.27 SW 108 0.026 -185.3 0.33 -59.2 -61.1 124.9 0.33 -63.3 -61.9 112.1 0.33 -64.7 -67 158.4 3.6 36 0.276 SW 109.5 0.026 -185.5 0.33 -61.8 -63.7 134.4 0.33 -65.9 -64.5 111.8 0.33 -67.3 -69.7 164.5 3.1 37 0.29 SW 109.8 0.027 -185.5 0.33 -64.5 -66.5 146 0.33 -68.6 -67.3 125.8 0.33 -69.8 -72.3 165.5 4.2 38 0.301 SW 109.9 0.027 -185.8 0.33 -66.8 -68.9 124.9 0.33 -71.5 -70.2 137.9 0.33 -72.6 -75.2 183.5 4.8 39 0.304 SW 112.8 0.027 -185.4 0.33 -69 -71.3 130.1 0.33 -73.5 -72.3 89.7 0.33 -74.9 -77.7 162.4 3.6 40 0.305
149
EXP 14 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 114.1 0.027 -185.6 0.33 -71.4 -73.6 129.5 0.33 -76.1 -74.8 122 0.33 -77.3 -80.3 171.5 3.2 41 0.242 SW 112.1 0.028 -185.3 0.33 -73.7 -76 130 0.33 -78.6 -77.4 123.1 0.33 -79.6 -82.7 164.4 3.5 42 0.316 SW 111.5 0.028 -185.9 0.33 -76.2 -78.5 142.9 0.33 -81 -79.9 120.5 0.33 -82 -85.2 177.9 2.4 43 0.305 SW 117.5 0.028 -185.7 0.33 -78.2 -80.7 122.2 0.33 -83.4 -82.3 120.5 0.33 -84.5 -87.7 179.5 4.2 44 0.308 SW 117.9 0.028 -186 0.33 -80.2 -82.8 119.1 0.33 -85.5 -84.5 112.4 0.33 -86.5 -90 163.1 4.4 45 0.248 SW 123.6 0.029 -185.3 0.33 -82.3 -85 129.3 0.33 -87.7 -86.7 107.7 0.33 -88.6 -92.2 169 3.4 46 0.28 SW 126.5 0.029 -185.8 0.33 -84.1 -86.9 115.3 0.33 -89.7 -88.7 98.9 0.33 -90.9 -94.5 180.7 4.1 47 0.258 SW 128.7 0.03 -185.4 0.33 -86.4 -89.1 134 0.33 -92.1 -91.1 131.1 0.33 -93 -96.9 181.7 4.5 48 0.287 SW 130.5 0.03 -185 0.33 -88.5 -91.4 137.8 0.33 -94.1 -93.2 108.7 0.33 -94.9 -98.9 168.4 4.6 49 0.278 SW 135.6 0.031 -185.5 0.33 -89.9 -92.9 92.1 0.33 -96 -95.1 103.8 0.33 -96.9 -101 177.1 4.6 50 0.293 SW 131.1 0.031 -185 0.33 -91.7 -94.8 121.9 0.33 -97.7 -96.7 81.5 0.33 -98.9 -103.1 180.6 5.0 51 0.255 SW 129.9 0.032 -185.5 0.33 -93.7 -96.9 131.4 0.33 -99.6 -98.8 117.9 0.33 -100.5 -104.9 157 5.3 52 0.261 SW 136.9 0.032 -185.3 0.33 -95.5 -98.7 116.8 0.33 -101.5 -100.7 109.3 0.33 -102.3 -106.7 170.9 4.4 53 0.24 SW 135.9 0.033 -185.7 0.33 -97.3 -100.6 126.3 0.33 -103.6 -102.7 111.4 0.33 -104.5 -108.9 202.3 5.6 54 0.3 SW 133.7 0.034 -185.5 0.33 -99 -102.3 112.1 0.33 -105.5 -104.7 119.4 0.33 -106.2 -110.8 174.7 2.6 55 0.294 SW 136.2 0.035 -185.6 0.33 -100.4 -103.9 106.4 0.33 -106.8 -106.2 84.6 0.33 -107.4 -112.3 148.8 4.4 56 0.232 SW 138.8 0.036 -185.5 0.33 -102.1 -105.5 110 0.33 -108.6 -108 113.6 0.33 -109.1 -113.9 168 4.0 57 0.26 SW 142.4 0.036 -185.8 0.33 -103.7 -107.2 121.8 0.33 -110 -109.5 88.1 0.33 -110.5 -115.4 162.9 5.6 58 0.302 SW 139.2 0.037 -185.4 0.33 -105.2 -108.8 114 0.33 -111.4 -111 90.2 0.33 -111.9 -116.9 158.7 5.3 59 0.289 SW 141.7 0.037 -185.4 0.33 -106.8 -110.5 120.3 0.33 -113.2 -112.7 112.2 0.33 -113.6 -118.6 182.5 5.8 60 0.222 SW 137.4 0.038 -185.2 0.33 -108.4 -112.1 122.7 0.33 -114.6 -114.4 110.3 0.33 -114.7 -120 152.2 2.3 61 0.221 SW 145.8 0.039 -185.9 0.33 -109.9 -113.7 120.3 0.33 -116.4 -116 105.6 0.33 -116.6 -121.8 198.9 2.0 62 0.289 SW 142 0.039 -185.7 0.33 -110.9 -114.9 88.4 0.33 -117.2 -117.1 66.1 0.33 -117.4 -122.8 130.9 4.4 63 0.257 SW 142.2 0.04 -185.5 0.33 -112.7 -116.6 133.8 0.33 -118.9 -118.7 119 0.33 -118.8 -124.2 169.1 2.9 64 0.259 SW 144.5 0.04 -185.6 0.33 -113.8 -117.9 101.3 0.33 -120.1 -120.1 86.5 0.33 -120.1 -125.6 168.5 5.9 65 0.258 SW 143.1 0.042 -185.5 0.33 -115.5 -119.5 130.5 0.33 -122.1 -121.9 140.2 0.33 -122 -127.4 208.1 2.5 66 0.259 SW 143.8 0.043 -185.7 0.33 -116.4 -120.7 91.7 0.33 -122.8 -122.9 65.2 0.33 -122.6 -128.4 135.9 3.4 67 0.277 SW 144.3 0.044 -185.6 0.33 -118.3 -122.4 153.8 0.33 -124.2 -124.3 103.4 0.33 -123.8 -129.5 158 6.4 68 0.27 SW 139.2 0.046 -185.5 0.33 -119.1 -123.4 76.2 0.33 -125.5 -125.7 109 0.33 -125 -130.7 163.1 2.7 69 0.263 SW 144.9 0.047 -185.5 0.33 -120 -124.4 89.3 0.33 -126.5 -126.6 64.8 0.33 -126.2 -132 176.3 3.3 70 0.249 SW 141.1 0.046 -185.4 0.33 -121.5 -125.8 129 0.33 -127.8 -128 114.5 0.33 -127.2 -133.1 156.8 3.6 71 0.245 SW 142.3 0.048 -185.3 0.33 -122.4 -126.9 90.7 0.33 -129 -129.2 98 0.33 -128.5 -134.4 181.5 3.8 72 0.257 SW 142.9 0.05 -185.5 0.33 -123.6 -128.1 111.8 0.33 -129.8 -130.2 68.9 0.33 -129.2 -135.3 145.4 4.8 73 0.248 SW 143.2 0.05 -185.8 0.33 -125.4 -129.8 157 0.33 -131.8 -132 164.3 0.33 -131 -136.9 222.5 3.4 74 0.278 SW 133.8 0.051 -185.8 0.33 -126.5 -131.1 120.1 0.33 -132.7 -133.2 101.5 0.33 -131.7 -137.9 149.1 6.8 75 0.319 SW 139.5 0.052 -185.9 0.33 -128 -132.5 142.9 0.33 -133.9 -134.6 132.6 0.33 -132.5 -138.8 144.5 2.5 76 0.296 SW 138.9 0.052 -185.9 0.33 -128.5 -133.3 73.6 0.33 -134.7 -135.5 80.1 0.33 -133.5 -139.7 158.6 6.0 77 0.305 SW 134.7 0.053 -185.9 0.33 -130 -134.7 142.8 0.33 -135.6 -136.5 100.5 0.33 -133.9 -140.3 114.2 6.9 78 0.258
150
EXP 14 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 114.1 0.027 -185.6 0.33 -71.4 -73.6 129.5 0.33 -76.1 -74.8 122 0.33 -77.3 -80.3 171.5 3.2 41 0.242 SW 112.1 0.028 -185.3 0.33 -73.7 -76 130 0.33 -78.6 -77.4 123.1 0.33 -79.6 -82.7 164.4 3.5 42 0.316 SW 111.5 0.028 -185.9 0.33 -76.2 -78.5 142.9 0.33 -81 -79.9 120.5 0.33 -82 -85.2 177.9 2.4 43 0.305 SW 117.5 0.028 -185.7 0.33 -78.2 -80.7 122.2 0.33 -83.4 -82.3 120.5 0.33 -84.5 -87.7 179.5 4.2 44 0.308 SW 117.9 0.028 -186 0.33 -80.2 -82.8 119.1 0.33 -85.5 -84.5 112.4 0.33 -86.5 -90 163.1 4.4 45 0.248 SW 123.6 0.029 -185.3 0.33 -82.3 -85 129.3 0.33 -87.7 -86.7 107.7 0.33 -88.6 -92.2 169 3.4 46 0.28 SW 126.5 0.029 -185.8 0.33 -84.1 -86.9 115.3 0.33 -89.7 -88.7 98.9 0.33 -90.9 -94.5 180.7 4.1 47 0.258 SW 128.7 0.03 -185.4 0.33 -86.4 -89.1 134 0.33 -92.1 -91.1 131.1 0.33 -93 -96.9 181.7 4.5 48 0.287 SW 130.5 0.03 -185 0.33 -88.5 -91.4 137.8 0.33 -94.1 -93.2 108.7 0.33 -94.9 -98.9 168.4 4.6 49 0.278 SW 135.6 0.031 -185.5 0.33 -89.9 -92.9 92.1 0.33 -96 -95.1 103.8 0.33 -96.9 -101 177.1 4.6 50 0.293 SW 131.1 0.031 -185 0.33 -91.7 -94.8 121.9 0.33 -97.7 -96.7 81.5 0.33 -98.9 -103.1 180.6 5.0 51 0.255 SW 129.9 0.032 -185.5 0.33 -93.7 -96.9 131.4 0.33 -99.6 -98.8 117.9 0.33 -100.5 -104.9 157 5.3 52 0.261 SW 136.9 0.032 -185.3 0.33 -95.5 -98.7 116.8 0.33 -101.5 -100.7 109.3 0.33 -102.3 -106.7 170.9 4.4 53 0.24 SW 135.9 0.033 -185.7 0.33 -97.3 -100.6 126.3 0.33 -103.6 -102.7 111.4 0.33 -104.5 -108.9 202.3 5.6 54 0.3 SW 133.7 0.034 -185.5 0.33 -99 -102.3 112.1 0.33 -105.5 -104.7 119.4 0.33 -106.2 -110.8 174.7 2.6 55 0.294 SW 136.2 0.035 -185.6 0.33 -100.4 -103.9 106.4 0.33 -106.8 -106.2 84.6 0.33 -107.4 -112.3 148.8 4.4 56 0.232 SW 138.8 0.036 -185.5 0.33 -102.1 -105.5 110 0.33 -108.6 -108 113.6 0.33 -109.1 -113.9 168 4.0 57 0.26 SW 142.4 0.036 -185.8 0.33 -103.7 -107.2 121.8 0.33 -110 -109.5 88.1 0.33 -110.5 -115.4 162.9 5.6 58 0.302 SW 139.2 0.037 -185.4 0.33 -105.2 -108.8 114 0.33 -111.4 -111 90.2 0.33 -111.9 -116.9 158.7 5.3 59 0.289 SW 141.7 0.037 -185.4 0.33 -106.8 -110.5 120.3 0.33 -113.2 -112.7 112.2 0.33 -113.6 -118.6 182.5 5.8 60 0.222 SW 137.4 0.038 -185.2 0.33 -108.4 -112.1 122.7 0.33 -114.6 -114.4 110.3 0.33 -114.7 -120 152.2 2.3 61 0.221 SW 145.8 0.039 -185.9 0.33 -109.9 -113.7 120.3 0.33 -116.4 -116 105.6 0.33 -116.6 -121.8 198.9 2.0 62 0.289 SW 142 0.039 -185.7 0.33 -110.9 -114.9 88.4 0.33 -117.2 -117.1 66.1 0.33 -117.4 -122.8 130.9 4.4 63 0.257 SW 142.2 0.04 -185.5 0.33 -112.7 -116.6 133.8 0.33 -118.9 -118.7 119 0.33 -118.8 -124.2 169.1 2.9 64 0.259 SW 144.5 0.04 -185.6 0.33 -113.8 -117.9 101.3 0.33 -120.1 -120.1 86.5 0.33 -120.1 -125.6 168.5 5.9 65 0.258 SW 143.1 0.042 -185.5 0.33 -115.5 -119.5 130.5 0.33 -122.1 -121.9 140.2 0.33 -122 -127.4 208.1 2.5 66 0.259 SW 143.8 0.043 -185.7 0.33 -116.4 -120.7 91.7 0.33 -122.8 -122.9 65.2 0.33 -122.6 -128.4 135.9 3.4 67 0.277 SW 144.3 0.044 -185.6 0.33 -118.3 -122.4 153.8 0.33 -124.2 -124.3 103.4 0.33 -123.8 -129.5 158 6.4 68 0.27 SW 139.2 0.046 -185.5 0.33 -119.1 -123.4 76.2 0.33 -125.5 -125.7 109 0.33 -125 -130.7 163.1 2.7 69 0.263 SW 144.9 0.047 -185.5 0.33 -120 -124.4 89.3 0.33 -126.5 -126.6 64.8 0.33 -126.2 -132 176.3 3.3 70 0.249 SW 141.1 0.046 -185.4 0.33 -121.5 -125.8 129 0.33 -127.8 -128 114.5 0.33 -127.2 -133.1 156.8 3.6 71 0.245 SW 142.3 0.048 -185.3 0.33 -122.4 -126.9 90.7 0.33 -129 -129.2 98 0.33 -128.5 -134.4 181.5 3.8 72 0.257 SW 142.9 0.05 -185.5 0.33 -123.6 -128.1 111.8 0.33 -129.8 -130.2 68.9 0.33 -129.2 -135.3 145.4 4.8 73 0.248 SW 143.2 0.05 -185.8 0.33 -125.4 -129.8 157 0.33 -131.8 -132 164.3 0.33 -131 -136.9 222.5 3.4 74 0.278 SW 133.8 0.051 -185.8 0.33 -126.5 -131.1 120.1 0.33 -132.7 -133.2 101.5 0.33 -131.7 -137.9 149.1 6.8 75 0.319 SW 139.5 0.052 -185.9 0.33 -128 -132.5 142.9 0.33 -133.9 -134.6 132.6 0.33 -132.5 -138.8 144.5 2.5 76 0.296 SW 138.9 0.052 -185.9 0.33 -128.5 -133.3 73.6 0.33 -134.7 -135.5 80.1 0.33 -133.5 -139.7 158.6 6.0 77 0.305 SW 134.7 0.053 -185.9 0.33 -130 -134.7 142.8 0.33 -135.6 -136.5 100.5 0.33 -133.9 -140.3 114.2 6.9 78 0.258
151
EXP 14 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 136.2 0.053 -185.8 0.33 -131 -135.9 119.5 0.33 -136.6 -137.5 99.1 0.33 -134.9 -141.3 158.6 3.2 79 0.33 SW 134 0.054 -185.5 0.33 -131.6 -136.8 99.3 0.33 -136.9 -138 28 0.33 -135.6 -142 137.2 4.2 80 0.254 SW 135.1 0.055 -185.4 0.33 -132.4 -137.5 78.3 0.33 -138.2 -139.2 131.1 0.33 -136.6 -143 165.2 5.7 81 0.271 SW 138.8 0.057 -185.6 0.33 -134 -138.9 158.4 0.33 -140 -140.7 159.5 0.33 -138.4 -144.7 256.6 2.9 82 0.297 SW 140.6 0.057 -185.6 0.33 -135 -140 124.1 0.33 -140.8 -141.9 124.8 0.33 -138.9 -145.5 139.7 3.0 83 0.293 SW 135.3 0.058 -186 0.33 -136.5 -141.5 176.7 0.33 -141.8 -143 130.2 0.33 -139.6 -146.3 149.7 2.6 84 0.278 SW 140.2 0.059 -186 0.33 -137.2 -142.4 100.1 0.33 -142.7 -143.9 105.4 0.33 -140.6 -147.2 171.5 2.6 85 0.291 SW 140.8 0.066 -185.6 0.33 -138.1 -143.4 124.7 0.33 -143.1 -144.6 81 0.33 -140.8 -147.6 98.1 5.8 86 0.272 SW 143.3 0.066 -185.8 0.33 -138.3 -143.9 66.7 0.33 -143.4 -144.9 27.1 0.33 -141.3 -148.1 117.1 2.4 87 0.343 SW 145.4 0.069 -186 0.33 -139.9 -145 157.4 0.33 -145.8 -146.7 230.5 0.33 -143.7 -150.1 336.8 5.9 88 0.296 SW 140.5 0.071 -185.2 0.33 -140.5 -146 120.8 0.33 -145.5 -147.1 31.1 0.33 -143.2 -150 53.2 2.8 89 0.272 SW 147.3 0.074 -185.8 0.33 -141.1 -146.5 75.2 0.33 -147.1 -148.2 140.4 0.33 -145.2 -151.8 285.9 4.1 90 0.249 SW 143.4 0.075 -185.7 0.33 -142.3 -147.8 185.5 0.33 -147.2 -148.8 62.5 0.33 -144.9 -151.5 79.1 5.8 91 0.256 SW 140.4 0.076 -185.6 0.33 -142.3 -147.6 42.2 0.33 -147.4 -149 8.4 0.33 -145.4 -152.5 133 3.3 92 0.241 SW 144.5 0.076 -185.9 0.33 -143.5 -148.9 126.7 0.33 -149.5 -150.6 242.9 0.33 -147.2 -153.9 280.6 3.4 93 0.273 SW 143.4 0.077 -185.5 0.33 -144.7 -150.3 202.8 0.33 -149.5 -151.2 66.2 0.33 -146.8 -153.9 67.8 4.7 94 0.297 SW 141.9 0.076 -185.5 0.33 -144.8 -150.6 50 0.33 -149.9 -151.6 61.1 0.33 -147.4 -154.5 142.3 2.9 95 0.282 SW 139.9 0.076 -185.4 0.33 -145.4 -151.1 76.3 0.33 -151.2 -152.6 138.3 0.33 -148.8 -155.7 258.6 6.0 96 0.281 SW 142.2 0.076 -186 0.33 -147.1 -152.5 221 0.33 -152.5 -154 220.7 0.33 -149.7 -156.7 216.8 2.5 97 0.259 SW 140 0.077 -185.9 0.33 -147.7 -153.5 153.1 0.33 -152.4 -154.5 64.4 0.33 -149.4 -156.8 56.5 5.1 98 0.295 SW 138.6 0.076 -185.6 0.33 -147.7 -153.2 48.4 0.33 -152.6 -154.5 38.3 0.33 -149.7 -157 106.8 3.6 99 0.297 SW 136.8 0.076 -185.8 0.33 -149.3 -154.9 196.1 0.33 -154.9 -156.3 279.3 0.33 -152.2 -159 400.9 4.0 100 0.256 SW 140.7 0.076 -185.8 0.33 -150 -155.9 179.9 0.33 -154.8 -156.8 53.3 0.33 -151.9 -158.9 105.4 2.5 101 0.263 SW 130.5 0.074 -185.4 0.33 -150.3 -155.9 106.9 0.33 -155 -156.5 32.1 0.33 -152.1 -158.7 115.8 2.6 102 0.256 SW 132.8 0.075 -185.7 0.33 -150.8 -156.7 55.8 0.33 -156.4 -158.1 214.9 0.33 -153.4 -160.6 260.7 2.2 103 0.295 SW 138.5 0.076 -185.8 0.33 -152.1 -158 252.8 0.33 -156.7 -158.7 97 0.33 -153.5 -160.3 123.4 2.3 104 0.289 SW 129.4 0.074 -185.9 0.33 -152.2 -157.6 82.2 0.33 -157.3 -159.1 66.6 0.33 -154.6 -161.9 266.6 2.8 105 0.23 SW 135.3 0.052 -185.6 0.42 -154.1 -159.3 166.8 0.42 -166.8 -164.7 1254.8 0.17 -175 -179.5 4428.8 3.7 106 0.167 SW 140.6 0.095 -185.5 0.42 -156.8 -158.9 13.5 0.42 -181.8 -178.7 4871.3 0.17 -177.8 -183.3 10622.9 3.2 107 0.265 SW 139.8 0.076 -185.8 -162 -184.7 -185.6 5.4 108 0.246 SW 138.3 0.077 -185.6 -166 -185.1 -184.4 6.0 109 0.188 SW 136.8 0.078 -185.4 -171.6 -185.4 -185.3 4.6 110 0.226 SW 135.4 0.078 -185.7 -179.4 -185.7 -184.8 5.2 111 0.23
152
EXP 15 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 83.3 1 8.2 0.33 21.73 22.4 497.6 0.33 22.33 22.9 282.7 0.33 21.95 23.2 142.2 0.0 1 0.317 N 83.7 1 5.7 0.33 20.99 21.5 348 0.33 21.5 22.2 220.6 0.33 20.84 22.2 367.2 0.0 2 0.31 N 84.2 1 3.3 0.33 20.27 20.8 255.7 0.33 20.6 21.2 320.6 0.33 20.15 21.5 249.7 0.0 3 0.282 N 88.5 1 0.6 0.33 19.35 19.8 325 0.33 19.97 20.6 159.3 0.33 19.4 20.7 232.3 0.0 4 0.295 N 88.6 1 -2.9 0.33 18.23 18.7 300 0.33 18.66 19.5 267.3 0.33 18 19.4 337.3 0.0 5 0.328 N 90.5 1 -7.9 0.33 16.62 17.1 375.5 0.33 17.34 18.1 298.3 0.33 16.95 18.2 250 0.0 6 0.336 N 91.7 1 -13.1 0.33 15.08 15.5 374.1 0.33 15.85 16.7 261.7 0.33 15.3 16.7 340.4 0.0 7 0.38
SW 90.7 1 -16.3 0.33 13.81 14.1 297.9 0.33 14.61 15.4 218.7 0.33 14.06 15.3 262.6 3.4 8 0.328 SW 93.2 1 -20.8 0.33 12.21 12.5 296.4 0.33 12.84 13.7 271.9 0.33 12.34 13.6 298.9 3.0 9 0.362 SW 92.4 1 -26.1 0.33 10.15 10.5 294.1 0.33 11.1 11.9 219.2 0.33 10.78 11.9 216.5 3.9 10 0.375 SW 97.3 1 -41 0.33 8.157 8.4 253.3 0.33 9.003 9.9 199 0.33 8.528 9.8 252.2 4.1 11 0.355 SW 95.6 0.015 -51.5 0.33 5.558 5.8 335 0.33 6.331 7.5 281.7 0.33 5.852 7.1 327.3 5.1 12 0.377 SW 97.1 0.014 -49.1 0.33 3.559 3.6 211.6 0.33 4.253 5.2 181.6 0.33 3.835 4.9 205.2 4.1 13 0.306 SW 102.2 0.014 -70.9 0.33 0.387 0.6 334.7 0.33 0.994 2.3 285.2 0.33 0.538 1.8 333.3 4.5 14 0.402 SW 92.9 0.014 -64.3 0.33 -2.01 -2.1 295.7 0.33 -1.25 -0.2 209.3 0.33 -1.84 -0.9 276.7 4.8 15 0.382 SW 99.6 0.014 -67.2 0.33 -5.17 -5.3 375.5 0.33 -4.38 -3.2 300.5 0.33 -4.87 -4 346.5 5.5 16 0.394 SW 96.9 0.014 -64.7 0.33 -7.29 -7.7 224.3 0.33 -6.77 -5.7 198.9 0.33 -7.2 -6.6 233.6 5.8 17 0.398 SW 101.3 0.014 -83.4 0.33 -10.3 -10.6 257.5 0.33 -9.65 -8.6 212.1 0.33 -9.88 -9.3 229.8 5.6 18 0.363 SW 103.4 0.013 -92.8 0.33 -13.5 -13.9 252.5 0.33 -13.2 -11.9 216.5 0.33 -13.6 -12.9 275.6 5.2 19 0.355 SW 104 0.013 -104.6 0.33 -16.5 -17 216.1 0.33 -16.2 -15 184.1 0.33 -16.5 -16.1 212.4 7.0 20 0.336 SW 106.2 0.013 -118.5 0.33 -19.8 -20.3 208 0.33 -19.8 -18.5 185.9 0.33 -20.1 -19.7 218.7 6.3 21 0.346 SW 109.2 0.013 -133.1 0.33 -23.2 -23.7 151.5 0.33 -23.5 -22.2 148.6 0.33 -23.7 -23.5 165.5 5.7 22 0.361 SW 118.4 0.013 -178.7 0.33 -27 -27.6 169.2 0.33 -27.4 -26 144.7 0.33 -27.7 -27.5 175.7 4.3 23 0.382 SW 104 0.014 -186.4 0.33 -30.2 -31 151 0.33 -30.8 -29.6 135.3 0.33 -31.1 -31.2 162.8 6.7 24 0.374 SW 113.6 0.013 -185.4 0.33 -33.2 -34.2 141.9 0.33 -34.1 -33 133.9 0.33 -34.3 -34.7 153.9 5.9 25 0.328 SW 114 0.013 -186.4 0.33 -37.2 -38.1 178 0.33 -38.1 -36.8 157.8 0.33 -38.3 -38.7 185.9 5.7 26 0.421 SW 121.1 0.013 -185.3 0.33 -40.6 -41.6 166.2 0.33 -41.7 -40.5 151.2 0.33 -41.9 -42.5 179 5.5 27 0.318 SW 113.1 0.013 -185.2 0.33 -43.8 -45.1 160.2 0.33 -45.3 -44.1 147.3 0.33 -45.5 -46.3 182.1 6.3 28 0.363 SW 118.7 0.014 -186.1 0.33 -48.2 -49.2 201.9 0.33 -49.9 -48.5 193.1 0.33 -49.9 -50.7 217.6 5.5 29 0.342 SW 123.2 0.013 -186.1 0.33 -51.6 -53 178.2 0.33 -53.5 -52.3 166 0.33 -53.5 -54.7 197 5.0 30 0.394 SW 121.8 0.013 -186.1 0.33 -54.8 -56.4 168.3 0.33 -56.9 -55.9 156 0.33 -56.8 -58.3 184.7 5.7 31 0.421 SW 126.9 0.013 -185.9 0.33 -57.8 -59.6 160.4 0.33 -60 -59.1 143.5 0.33 -60.1 -61.8 183.4 5.3 32 0.316 SW 127.8 0.013 -186.4 0.33 -60.8 -62.7 160.9 0.33 -63.4 -62.5 154.6 0.33 -63.4 -65.2 190.4 4.9 33 0.421 SW 132.5 0.014 -185.9 0.33 -63.7 -65.8 165.3 0.33 -66 -65.3 124.9 0.33 -66 -68.2 165 5.7 34 0.349 SW 133.5 0.014 -186.5 0.33 -66.6 -68.7 154 0.33 -69.3 -68.5 156.1 0.33 -69.1 -71.4 180.7 6.2 35 0.369 SW 134.3 0.014 -186.1 0.33 -69.4 -71.6 161.2 0.33 -71.8 -71.4 140.1 0.33 -71.4 -73.9 151.4 6.0 36 0.378 SW 133.9 0.014 -185.8 0.33 -71.8 -74.2 141.4 0.33 -74.9 -74.2 135.3 0.33 -74.8 -77.3 202.2 4.5 37 0.391 SW 138 0.014 -186.4 0.33 -74.9 -77.3 175.3 0.33 -77.7 -77.2 150.6 0.33 -77.3 -80 167.6 2.7 38 0.398
153
EXP 15 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 137.8 0.014 -186.6 0.33 -77 -79.7 135.4 0.33 -80.6 -79.9 134.6 0.33 -80.6 -83.4 212.4 4.5 39 0.364 SW 137.3 0.014 -186 0.33 -79.7 -82.4 159.6 0.33 -82.9 -82.5 132.3 0.33 -82.6 -85.8 154.7 4.9 40 0.381 SW 138.6 0.014 -186.6 0.33 -82.3 -85.1 164.9 0.33 -85.4 -85.2 146.6 0.33 -84.6 -88 148.7 4.3 41 0.398 SW 141.5 0.014 -186.3 0.33 -84.9 -87.6 153.9 0.33 -88.4 -88.2 170.9 0.33 -87.5 -90.8 190.6 5.8 42 0.419 SW 142 0.014 -186.2 0.33 -87.3 -90.3 161.5 0.33 -91 -90.6 128.7 0.33 -90.6 -94 216.9 2.9 43 0.413 SW 145 0.015 -186.5 0.33 -89.5 -92.5 141.3 0.33 -93.5 -93.3 156.3 0.33 -92.7 -96.4 168.2 5.4 44 0.399 SW 146 0.015 -186.4 0.33 -91.8 -94.9 157.2 0.33 -95.4 -95.4 120 0.33 -94.6 -98.5 157.8 5.0 45 0.411 SW 147.3 0.015 -186.2 0.33 -93.9 -97.2 145.5 0.33 -97.8 -97.7 135.1 0.33 -97 -100.9 181.8 5.7 46 0.417 SW 151.7 0.015 -186 0.33 -96.1 -99.4 150.1 0.33 -100 -100.1 146.7 0.33 -99.4 -103.4 190.6 6.3 47 0.373 SW 150.2 0.015 -186.4 0.33 -98.7 -102 181.1 0.33 -103 -102.8 175.4 0.33 -101 -105.5 161 3.9 48 0.388 SW 149.8 0.015 -185.6 0.33 -100 -103.9 125.6 0.33 -104 -104.3 87.2 0.33 -103 -107.5 163 5.5 49 0.381 SW 154.5 0.016 -186.2 0.33 -103 -106.1 159.3 0.33 -107 -107 188.5 0.33 -105 -109.8 189.9 2.7 50 0.378 SW 152.6 0.016 -186.4 0.33 -104 -107.8 119.6 0.33 -109 -109 134.1 0.33 -107 -112 184.5 5.0 51 0.397 SW 156.3 0.016 -186.2 0.33 -106 -109.7 149 0.33 -110 -110.3 73.2 0.33 -109 -113.4 128.7 3.0 52 0.393 SW 159.4 0.016 -186.1 0.33 -108 -111.8 157.7 0.33 -113 -112.9 202.4 0.33 -111 -115.5 190.1 6.5 53 0.356 SW 161.7 0.017 -186.4 0.33 -109 -113.2 101.9 0.33 -114 -114.5 109.4 0.33 -112 -117.3 154.6 4.5 54 0.408 SW 163.8 0.017 -186.2 0.33 -111 -114.9 130.1 0.33 -115 -115.8 86.3 0.33 -114 -118.9 156.3 5.5 55 0.351 SW 166.9 0.017 -186 0.33 -113 -116.8 154.9 0.33 -117 -117.5 125.4 0.33 -116 -120.7 172.1 5.3 56 0.32 SW 167.3 0.018 -186.2 0.33 -114 -118.5 140.9 0.33 -119 -119.2 125.9 0.33 -117 -122.2 155 5.9 57 0.367 SW 165.3 0.018 -186.2 0.33 -116 -120.2 140.4 0.33 -120 -121 138.8 0.33 -119 -124.1 194.2 4.9 58 0.382 SW 168.9 0.018 -186.6 0.33 -117 -121.9 144.4 0.33 -122 -122.5 114.6 0.33 -120 -125.4 135.4 4.6 59 0.359 SW 170.4 0.019 -186.6 0.33 -119 -123.4 130.8 0.33 -124 -124.3 146.3 0.33 -122 -127.1 174.7 5.1 60 0.372 SW 172.3 0.019 -186.8 0.33 -120 -124.7 118.7 0.33 -125 -125.7 118.6 0.33 -123 -128.4 144.9 6.0 61 0.304 SW 178.7 0.02 -186.3 0.33 -121 -126 121 0.33 -126 -127 103.4 0.33 -125 -130.2 198.7 4.9 62 0.331 SW 176.3 0.02 -186.5 0.33 -123 -127.5 144.5 0.33 -127 -128.3 103 0.33 -125 -131.3 129.8 3.1 63 0.327 SW 182.4 0.02 -186 0.33 -124 -128.4 83.9 0.33 -128 -129.4 91.4 0.33 -127 -132.5 156.6 6.3 64 0.302 SW 177 0.021 -186.3 0.33 -125 -129.6 115.6 0.33 -130 -130.6 100.9 0.33 -128 -133.7 152.7 6.1 65 0.323 SW 183.9 0.022 -186.5 0.33 -127 -131.4 184.8 0.33 -132 -132.6 202.8 0.33 -130 -135.5 215.4 6.2 66 0.342 SW 183.6 0.023 -186.4 0.33 -127 -132.5 100.8 0.33 -132 -133.2 32.9 0.33 -130 -136.2 101.3 4.7 67 0.308 SW 186.3 0.023 -186.2 0.33 -128 -133.4 101.4 0.33 -133 -134.5 125.2 0.33 -131 -137.3 156.9 3.0 68 0.327 SW 187.2 0.023 -186.5 0.33 -130 -134.6 129.8 0.33 -134 -135.5 88.7 0.33 -133 -138.7 179.1 6.3 69 0.341 SW 185.6 0.024 -186.4 0.33 -131 -136.3 176.7 0.33 -136 -137.2 173.8 0.33 -134 -140.3 212.7 6.1 70 0.337 SW 181.3 0.024 -186.5 0.33 -132 -137.2 96.3 0.33 -136 -138 64.3 0.33 -134 -140.7 82.1 4.0 71 0.36 SW 182.8 0.025 -186.3 0.33 -133 -137.9 81.6 0.33 -138 -138.9 94.1 0.33 -136 -141.9 181.8 6.5 72 0.362 SW 179.6 0.025 -186.5 0.33 -134 -139.3 164.9 0.33 -139 -140.3 153 0.33 -137 -143.2 190.6 5.6 73 0.376 SW 185.3 0.026 -186.3 0.33 -135 -140.4 135.7 0.33 -139 -141.1 73.1 0.33 -137 -143.6 75.5 4.3 74 0.368 SW 181.4 0.026 -186.5 0.33 -137 -141.6 134.4 0.33 -142 -142.9 215.8 0.33 -139 -145.5 277.5 4.5 75 0.373 SW 184.2 0.027 -186.6 0.33 -138 -143.3 212.8 0.33 -143 -144.3 157.6 0.33 -140 -146.6 170.4 4.9 76 0.345
154
EXP 15 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 183.5 0.027 -186.5 0.33 -139 -144.6 147.4 0.33 -144 -145.6 168.4 0.33 -141 -147.6 158.3 3.8 77 0.399 SW 182.4 0.027 -186.4 0.33 -140 -145.5 120.5 0.33 -145 -146.6 113.7 0.33 -142 -148.7 185 6.5 78 0.374 SW 184.8 0.028 -186.8 0.33 -141 -146.5 135.1 0.33 -145 -146.8 26 0.33 -142 -148.5 45.7 5.4 79 0.395 SW 176.5 0.027 -186.6 0.33 -141 -146.8 45.8 0.33 -145 -147.4 77.7 0.33 -142 -149.2 103.8 2.8 80 0.37 SW 180.2 0.028 -186.8 0.33 -142 -147.8 157.4 0.33 -146 -148.3 132.3 0.33 -143 -150.1 161.7 8.5 81 0.399 SW 181.9 0.028 -186.4 0.33 -144 -149.4 228.1 0.33 -148 -149.6 176.1 0.33 -144 -151 155 4.1 82 0.396 SW 190.5 0.03 -186.4 0.33 -145 -150.2 112.7 0.33 -149 -151.1 197.8 0.33 -146 -152.8 302.8 4.5 83 0.38 SW 192 0.031 -186.6 0.33 -146 -151.9 248.3 0.33 -150 -152.4 192.3 0.33 -147 -153.7 148.2 4.8 84 0.369 SW 194.2 0.033 -186.9 0.33 -147 -153 167.3 0.33 -151 -153.4 149.3 0.33 -147 -154.4 144.3 6.6 85 0.395 SW 195.4 0.034 -186.9 0.33 -147 -153.1 35.2 0.33 -151 -152.6 34.3 0.33 -148 -153.4 85.5 5.8 86 0.396 SW 194.1 0.034 -186.8 0.33 -149 -154.9 286.5 0.33 -153 -155.2 275.4 0.33 -149 -155.8 207.4 3.0 87 0.367 SW 192.2 0.035 -186.5 0.33 -149 -155.3 59.6 0.33 -154 -156.3 188.5 0.33 -150 -157.3 265.9 6.0 88 0.376 SW 190.8 0.036 -187 0.33 -150 -155.6 77.5 0.33 -154 -155.2 57.6 0.33 -150 -155.9 65 6.4 89 0.386 SW 188.6 0.036 -186.8 0.33 -150 -156.3 125.9 0.33 -154 -156.3 95.4 0.33 -151 -156.5 94 6.1 90 0.407 SW 191.5 0.036 -186.7 0.33 -150 -156.5 58.1 0.33 -155 -156.3 50 0.33 -151 -157.1 59.4 4.7 91 0.392 SW 188.6 0.036 -186.6 0.33 -151 -156.5 53.8 0.33 -155 -157.5 79.8 0.33 -152 -158.9 219.3 4.1 92 0.376 SW 187.8 0.02 -186.3 0.42 -152 -158.1 260.7 0.42 -159 -159.5 344.2 0.17 -166 -171.4 2829 6.7 93 0.356 SW 180.7 0.038 -186.8 0.42 -157 -160.7 435.4 0.42 -173 -169.8 2383.5 0.17 -176 -181.2 4374.8 5.0 94 0.417 SW 186.9 0.035 -186.4 -160.7 -180.7 -183.5 5.5 95 0.371 SW 188.6 0.035 -186.6 -161.4 -181.4 -182.7 4.5 96 0.396 SW 181.9 0.035 -186.4 -168.3 -185.3 -184.7 3.6 97 0.395 SW 183.6 0.036 -187 -176.8 -184.5 -182.4 6.2 98 0.379 SW 183.1 0.036 -186.7 -185.3 -186 -183.5 5.1 99 0.386 SW 183.7 0.036 -186.6 -185.6 -185.7 -184.7 4.3 100 0.392 SW 182.2 0.036 -186.9 -188.1 -187.3 -185.2 4.5 101 0.394 SW 180.3 0.037 -186.9 -185.7 -183.4 -181.3 4.5 102 0.37 SW 180.3 0.037 -187.1 -187.7 -185.3 -182.7 7.1 103 0.389 SW 179.3 0.037 -186.8 -187.4 -186.3 -184.6 6.2 104 0.384 SW 180.1 0.037 -186.7 -186.1 -184.8 -183.2 5.2 105 0.375 SW 179.3 0.037 -186.7 -186.3 -185.2 -183.6 6.1 106 0.369 SW 176 0.037 -186.7 -186.3 -185 -183.6 4.5 107 0.343 SW 175.5 0.037 -186.4 -186.6 -185 -183.2 7.2 108 0.39 SW 171.1 0.037 -186.7 -187 -186 -184.7 6.1 109 0.36 SW 169.4 0.037 -187.3 -187.7 -185.8 -183.9 3.0 110 0.353 SW 165.6 0.038 -187 -186.5 -184.8 -183.3 6.9 111 0.348 SW 166.4 0.038 -186.9 -187.7 -186.8 -185.3 6.2 112 0.32 SW 167.2 0.038 -187 -187.5 -185.7 -183.3 6.9 113 0.314
155
EXP 16 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 83.7 1 12.2 0.33 22.94 23.7 656 0.33 23.27 24.1 401 0.33 22.48 24 508.5 0.0 1 0.377 N 84.1 1 9.2 0.33 22.47 23 255 0.33 22.56 23.4 243 0.33 21.66 23.1 356.4 0.0 2 0.311 N 81.9 1 5.2 0.33 21.34 21.9 385 0.33 21.46 22.5 274 0.33 20.42 21.9 416.9 0.0 3 0.382 N 88.9 1 1.4 0.33 20.25 20.8 354 0.33 20.44 21.4 280 0.33 19.5 20.9 313.1 0.0 4 0.355 N 84.3 1 -2.3 0.33 18.83 19.4 400 0.33 19.15 20.2 275 0.33 18.17 19.6 361.8 0.0 5 0.382 N 90.8 1 -6.6 0.33 17.32 17.8 376 0.33 17.49 18.7 305 0.33 16.38 17.8 422.3 0.0 6 0.373 N 87.4 1 -11.6 0.33 15.44 16 401 0.33 15.78 16.9 347 0.33 15.01 16.3 317.9 0.0 7 0.413 N 93.5 1 -17 0.33 13.5 13.9 374 0.33 13.98 15.2 238 0.33 12.93 14.3 362.6 0.0 8 0.421 N 93.5 1 -25.9 0.33 11.34 11.7 396 0.33 11.78 13.1 311 0.33 10.73 12.1 391 0.0 9 0.444 N 94.6 1 -28.3 0.33 9.008 9.3 414 0.33 9.401 10.8 314 0.33 8.23 9.6 428.6 0.0 10 0.395 N 96.4 1 -32.2 0.33 6.43 6.6 408 0.33 6.981 8.4 296 0.33 5.845 7.1 376.3 0.0 11 0.44 N 97 1 -40.1 0.33 3.416 3.6 458 0.33 3.974 5.6 339 0.33 2.743 4 452.7 0.0 12 0.443 N 97.1 1 -43.8 0.33 -0.11 0.1 411 0.33 0.55 2.3 315 0.33 -0.61 0.6 387.2 0.0 13 0.466 N 103.1 1 -61.2 0.33 -3.55 -3.6 348 0.33 -2.79 -1.1 258 0.33 -3.95 -2.8 327.6 0.0 14 0.43 N 100.7 1 -77.6 0.33 -7.02 -7.2 296 0.33 -6.37 -4.6 230 0.33 -7.58 -6.6 298.5 0.0 15 0.379 N 106.4 1 -94.6 0.33 -11.3 -11.4 347 0.33 -11.1 -9 305 0.33 -12.3 -11.1 376.1 0.0 16 0.42 N 103.1 1 -96.4 0.33 -15.1 -15.5 320 0.33 -14.8 -13 252 0.33 -15.8 -15.1 307.7 0.0 17 0.382 N 104.2 1 -104.1 0.33 -19.2 -19.6 286 0.33 -19.3 -17.3 253 0.33 -20.3 -19.6 311.4 0.0 18 0.411 N 111.7 1 -120.5 0.33 -23.4 -23.9 319 0.33 -23.7 -21.7 269 0.33 -24.8 -24.3 342.5 0.0 19 0.383 N 105 1 -116.8 0.33 -27.5 -28.1 279 0.33 -28.1 -26.2 258 0.33 -29.1 -28.8 305.8 0.0 20 0.35
SW 111 1 -129.9 0.33 -31.7 -32.4 277 0.33 -32.7 -30.8 248 0.33 -33.7 -33.6 312.3 3.7 21 0.397 SW 109.9 0.022 -137.7 0.33 -36 -36.7 199 0.33 -37.2 -35.3 184 0.33 -38 -38.1 212.2 4.4 22 0.356 SW 111.7 0.022 -183.2 0.33 -40 -41 197 0.33 -41.3 -39.6 170 0.33 -42 -42.5 206.7 2.3 23 0.365 SW 113.1 0.022 -184.7 0.33 -44.4 -45.4 210 0.33 -46.1 -44.2 193 0.33 -46.8 -47.3 234 2.9 24 0.4 SW 111.9 0.022 -185.6 0.33 -48.1 -49.4 193 0.33 -49.9 -48.4 171 0.33 -50.4 -51.4 202.3 1.9 25 0.35 SW 111.9 0.022 -185.3 0.33 -52.3 -53.6 209 0.33 -54.2 -52.6 184 0.33 -54.7 -55.8 228.8 3.3 26 0.374 SW 115.7 0.022 -184.7 0.33 -56 -57.6 198 0.33 -58.3 -56.8 184 0.33 -58.8 -60.1 228.2 3.3 27 0.348 SW 112.8 0.022 -185.2 0.33 -60.3 -61.9 223 0.33 -62.4 -61.1 200 0.33 -62.5 -64.1 217 3.3 28 0.384 SW 123.8 0.022 -184.7 0.33 -64 -65.8 205 0.33 -66.8 -65.4 205 0.33 -67 -68.6 252.4 2.8 29 0.414 SW 123.2 0.022 -184.7 0.33 -68 -69.8 220 0.33 -71 -69.6 197 0.33 -71.4 -73.2 262.1 2.6 30 0.385 SW 120.8 0.022 -185 0.33 -71.5 -73.6 204 0.33 -74.8 -73.5 195 0.33 -75 -77.2 235.9 3.4 31 0.432 SW 123.7 0.022 -185.3 0.33 -75.6 -77.7 234 0.33 -78.8 -77.7 219 0.33 -78.5 -81 228.7 3.8 32 0.417 SW 125.5 0.023 -185.4 0.33 -79.4 -81.6 228 0.33 -82.7 -81.7 204 0.33 -82.6 -85.1 262.1 3.6 33 0.422 SW 128.2 0.022 -185.4 0.33 -82.4 -85.1 203 0.33 -85.9 -85 173 0.33 -86 -88.9 244.5 3.6 34 0.434 SW 131.3 0.022 -184.8 0.33 -86 -88.6 215 0.33 -89.7 -88.9 223 0.33 -89.3 -92.4 239.9 3.4 35 0.436 SW 135.7 0.023 -184.9 0.33 -88.9 -91.7 197 0.33 -93.1 -92.3 190 0.33 -92.8 -96.1 255 3.7 36 0.393 SW 139.7 0.023 -185.1 0.33 -92.1 -95 210 0.33 -96.1 -95.6 191 0.33 -95.7 -99.2 226.1 4.1 37 0.418 SW 141.5 0.023 -185.2 0.33 -94.9 -97.9 189 0.33 -99.6 -98.9 200 0.33 -99.2 -102.8 264.6 3.3 38 0.379
156
EXP 16 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 141.5 0.024 -186 0.33 -98.1 -101.1 215 0.33 -103 -102.3 222 0.33 -102 -105.9 233.4 3.7 39 0.367 SW 144.3 0.024 -185 0.33 -100 -103.5 165 0.33 -105 -104.7 144 0.33 -105 -108.7 227.8 3.6 40 0.38 SW 146.2 0.024 -185.2 0.33 -103 -105.9 172 0.33 -108 -107.4 191 0.33 -107 -111.1 203.5 4.3 41 0.361 SW 151.4 0.025 -183.8 0.33 -105 -108.6 196 0.33 -111 -110.6 227 0.33 -110 -114.2 269.4 3.4 42 0.373 SW 154.4 0.025 -184.8 0.33 -108 -111 173 0.33 -113 -112.8 148 0.33 -112 -116.6 213.6 3.7 43 0.37 SW 153.9 0.026 -185.4 0.33 -110 -113.4 174 0.33 -115 -115.1 165 0.33 -114 -119 222.1 4.0 44 0.328 SW 150.5 0.026 -185.2 0.33 -112 -115.6 172 0.33 -117 -117.2 159 0.33 -116 -121.3 219 3.5 45 0.354 SW 158.7 0.027 -185.4 0.33 -114 -117.9 183 0.33 -120 -119.8 202 0.33 -119 -123.6 228.5 4.5 46 0.355 SW 164.2 0.027 -185.4 0.33 -116 -120 164 0.33 -122 -121.8 160 0.33 -120 -125.5 197.4 4.0 47 0.369 SW 163.5 0.028 -184.9 0.33 -118 -122 166 0.33 -124 -124.1 186 0.33 -123 -127.8 242.8 4.1 48 0.377 SW 163.6 0.028 -185.3 0.33 -120 -124.1 184 0.33 -126 -126.1 175 0.33 -124 -129.8 217.6 4.3 49 0.404 SW 165.2 0.028 -184.7 0.33 -122 -126.1 171 0.33 -128 -128.2 187 0.33 -126 -131.8 223.4 5.9 50 0.393 SW 162.9 0.029 -185.2 0.33 -124 -128.2 189 0.33 -130 -130.2 179 0.33 -128 -133.5 201.1 3.4 51 0.411 SW 162.6 0.029 -185.1 0.33 -126 -130.2 180 0.33 -131 -132.1 184 0.33 -130 -135.4 236.4 4.0 52 0.431 SW 161.3 0.029 -185.3 0.33 -128 -132.1 179 0.33 -133 -134.1 202 0.33 -131 -137 201.7 4.5 53 0.42 SW 164.6 0.029 -185.4 0.33 -130 -134.2 215 0.33 -135 -136.4 244 0.33 -133 -138.7 211.1 4.9 54 0.408 SW 162.1 0.03 -184.9 0.33 -131 -135.8 155 0.33 -136 -137.6 126 0.33 -134 -140.1 182.4 6.0 55 0.424 SW 163.3 0.03 -185.2 0.33 -133 -137.5 175 0.33 -139 -139.5 225 0.33 -136 -142.1 275.5 4.3 56 0.406 SW 162.2 0.03 -184.8 0.33 -134 -139.2 188 0.33 -140 -141 169 0.33 -137 -143.1 147.5 4.9 57 0.417 SW 167.3 0.031 -184.9 0.33 -136 -140.7 169 0.33 -141 -142.3 149 0.33 -139 -145.1 285.2 4.9 58 0.413 SW 163.9 0.031 -185 0.33 -137 -141.9 138 0.33 -143 -144.1 239 0.33 -139 -146 133.3 4.1 59 0.418 SW 161.9 0.032 -185.2 0.33 -139 -143.6 196 0.33 -144 -145.3 151 0.33 -141 -147.5 234.1 4.0 60 0.418 SW 166.7 0.034 -186 0.33 -140 -145.1 177 0.33 -145 -146.5 160 0.33 -142 -148.6 178.5 4.9 61 0.398 SW 174.7 0.035 -185.1 0.33 -141 -146.3 155 0.33 -147 -148.1 233 0.33 -144 -150.1 245.6 4.4 62 0.403 SW 177 0.038 -184.8 0.33 -142 -147.2 121 0.33 -147 -149 120 0.33 -144 -151.1 189.4 3.8 63 0.376 SW 182.9 0.04 -185 0.33 -143 -148.5 170 0.33 -149 -150.5 238 0.33 -146 -152.6 251.4 4.2 64 0.368 SW 185.5 0.043 -185.4 0.33 -144 -149.7 166 0.33 -150 -151.5 146 0.33 -147 -153.8 224 5.2 65 0.369 SW 192.5 0.046 -185.1 0.33 -145 -150.7 146 0.33 -151 -152.6 187 0.33 -148 -154.8 196.2 3.4 66 0.398 SW 197.3 0.047 -185 0.33 -146 -151.5 118 0.33 -152 -153.7 189 0.33 -149 -155.9 232.6 4.9 67 0.396 SW 186 0.044 -185 0.33 -147 -152.7 175 0.33 -153 -154.8 195 0.33 -150 -157 237.5 4.5 68 0.386 SW 179.8 0.042 -184.9 0.42 -149 -153.9 184 0.42 -156 -156.1 89 0.17 -167 -171.8 3424 4.4 69 0.412 SW 179.8 0.042 -184.9 0.42 -152 -155.1 137 0.42 -176 -171.4 3435 0.17 -176 -180.8 4652 4.6 70 0.373 SW 192.6 0.068 -185 -157.3 -180.7 -181.7 4.3 71 0.323 SW 192 0.05 -184.8 -166.4 -182.3 -182.3 5.2 72 0.343 SW 191.1 0.051 -185.2 -180.4 -183.4 -182.7 3.5 73 0.379 SW 197 0.055 -184.9 -182.4 -183.7 -182.9 3.6 74 0.315 SW 197.1 0.057 -184.7 -182.7 -184 -183.1 5.7 75 0.297 SW 191.7 0.057 -185 -183.1 -184.1 -183.1 3.3 76 0.358
157
EXP 16 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 184.7 0.058 -185.3 -183.5 -184.3 -183.2 4.1 77 0.301 SW 184.3 0.058 -185 -183.3 -184.4 -183.5 3.7 78 0.402 SW 184.6 0.058 -185 -183.6 -184.8 -183.8 5.5 79 0.284 SW 178.8 0.058 -185.3 -183.9 -185.2 -184.3 3.9 80 0.296 SW 174.5 0.059 -185.2 -183.9 -185.1 -184.3 5.1 81 0.27 SW 178 0.059 -185.5 -184.6 -185.3 -184 5.7 82 0.231 SW 170.7 0.06 -185.3 -184.6 -185.6 -184.5 4.5 83 0.262 SW 174.6 0.06 -185.4 -184.8 -185.5 -184.5 6.1 84 0.267
EXP 17 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 81.3 1 8.8 0.33 22.85 23.7 572 0.33 23.11 24 433 0.33 22.46 24 437.2 0.0 1 0.360 N 82.1 1 6.6 0.33 22.29 22.9 281 0.33 22.37 23.3 198 0.33 21.39 22.9 400.8 0.0 2 0.297 N 85.8 1 3.3 0.33 21.48 22 298 0.33 21.8 22.6 174 0.33 20.91 22.2 207.7 0.0 3 0.380 N 82.4 1 0.5 0.33 20.29 20.8 367 0.33 20.57 21.6 267 0.33 19.56 21 384 0.0 4 0.373 N 86.9 1 -2.3 0.33 19.42 19.9 262 0.33 19.57 20.5 235 0.33 18.6 19.9 289.9 0.0 5 0.301 N 88.3 1 -6.3 0.33 18.04 18.5 349 0.33 18.43 19.4 228 0.33 17.5 18.8 281.2 0.0 6 0.363 N 88.2 1 -10.4 0.33 16.77 17.1 305 0.33 17.14 18.2 218 0.33 16.13 17.4 302.4 0.0 7 0.399 N 87.3 1 -15.3 0.33 15.02 15.4 364 0.33 15.37 16.5 281 0.33 14.33 15.7 364.4 0.0 8 0.385 N 94.7 1 -19 0.33 13.63 13.9 250 0.33 14.12 15.1 171 0.33 13.12 14.3 218.7 0.0 9 0.399 N 94 1 -31.6 0.33 11.58 11.9 318 0.33 11.84 13.3 233 0.33 10.47 11.9 381.4 0.0 10 0.405 N 92.4 1 -34.6 0.33 9.337 9.6 332 0.33 10.02 11.2 229 0.33 8.978 10.1 246.2 0.0 11 0.387 N 91 1 -41.2 0.33 6.997 7.1 361 0.33 7.494 8.9 275 0.33 6.288 7.5 382 0.0 12 0.427
SW 95.7 0.036 -41 0.33 4.909 4.8 290 0.33 5.61 6.9 183 0.33 4.369 5.4 262.9 3.7 13 0.407 SW 95.2 0.036 -53.4 0.33 2.175 2.1 378 0.33 2.831 4.4 271 0.33 1.513 2.6 378 4.4 14 0.426 SW 98.4 0.035 -50.3 0.33 -0.23 -0.4 269 0.33 0.194 1.6 233 0.33 -0.94 0 277.1 2.3 15 0.376 SW 98.8 0.035 -67.7 0.33 -2.94 -3.2 250 0.33 -2.34 -0.9 171 0.33 -3.53 -2.7 235.5 2.9 16 0.413 SW 94.1 0.036 -85.4 0.33 -5.74 -6 203 0.33 -5.43 -3.9 171 0.33 -6.6 -5.8 217.9 1.9 17 0.410 SW 107 0.033 -107.7 0.33 -9.2 -9.4 265 0.33 -9.03 -7.3 213 0.33 -10.3 -9.4 282.2 3.3 18 0.407 SW 97.3 0.035 -102.2 0.33 -12.5 -12.8 211 0.33 -12.5 -10.8 177 0.33 -13.7 -13 221.3 3.3 19 0.410 SW 107.6 0.034 -127.1 0.33 -15.6 -16.1 204 0.33 -16 -14.2 176 0.33 -17.2 -16.7 232.4 3.3 20 0.336 SW 104.8 0.034 -129.3 0.33 -19.4 -19.9 246 0.33 -20 -18 200 0.33 -21.4 -20.9 277 2.8 21 0.371 SW 107.1 0.034 -128.1 0.33 -23 -23.6 237 0.33 -23.8 -21.9 208 0.33 -25 -24.8 250.6 2.6 22 0.379 SW 107 0.034 -132.4 0.33 -26.4 -27.1 157 0.33 -27.5 -25.7 140 0.33 -28.8 -28.7 180.2 3.4 23 0.403 SW 109.3 0.034 -181.6 0.33 -29.8 -30.7 157 0.33 -31 -29.3 134 0.33 -32.2 -32.5 169.6 3.8 24 0.341 SW 103.4 0.035 -186.2 0.33 -33.2 -34.2 157 0.33 -34.5 -32.8 129 0.33 -35.7 -36.2 172.4 3.6 25 0.379
158
EXP 17 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 114.1 0.034 -185.6 0.33 -36.9 -37.9 170 0.33 -38.2 -36.6 151 0.33 -39.2 -39.8 171.9 3.6 26 0.387 SW 108.5 0.034 -186 0.33 -40.3 -41.5 166 0.33 -42.1 -40.4 147 0.33 -43.1 -43.7 193.2 3.4 27 0.361 SW 109.3 0.035 -186.9 0.33 -43.7 -45 166 0.33 -45.7 -44.1 152 0.33 -46.6 -47.5 186.9 3.7 28 0.390 SW 115.9 0.034 -186.1 0.33 -47 -48.4 167 0.33 -49 -47.6 142 0.33 -49.7 -50.9 170.7 4.1 29 0.384 SW 114.6 0.034 -185.4 0.33 -50.5 -52 177 0.33 -52.7 -51.2 152 0.33 -53.5 -54.7 202.3 3.3 30 0.357 SW 114.2 0.034 -185 0.33 -53.8 -55.5 173 0.33 -56 -54.7 148 0.33 -56.7 -58.3 186.8 3.7 31 0.367 SW 118.3 0.035 -185.1 0.33 -56.8 -58.6 158 0.33 -59.7 -58.3 158 0.33 -60.4 -62 203 3.6 32 0.343 SW 121.1 0.034 -185.8 0.33 -60 -61.8 168 0.33 -62.8 -61.6 146 0.33 -63.4 -65.3 187.2 4.3 33 0.383 SW 124.7 0.034 -185.6 0.33 -62.7 -64.8 152 0.33 -66 -64.7 137 0.33 -66.7 -68.8 199.2 3.4 34 0.390 SW 127.1 0.035 -185.4 0.33 -65.7 -67.8 161 0.33 -69.3 -68.1 161 0.33 -69.9 -72.1 196 3.7 35 0.364 SW 128.1 0.035 -185.6 0.33 -68.4 -70.6 153 0.33 -72.1 -71 135 0.33 -72.8 -75.3 189.8 4.0 36 0.395 SW 130.9 0.035 -185.2 0.33 -71.1 -73.3 151 0.33 -75.1 -74 144 0.33 -75.6 -78.3 189.3 3.5 37 0.368 SW 130.1 0.036 -185.6 0.33 -73.6 -75.9 146 0.33 -77.9 -76.8 143 0.33 -78.4 -81.2 188.6 4.5 38 0.369 SW 133.6 0.036 -185.2 0.33 -76.3 -78.6 154 0.33 -80.9 -79.8 150 0.33 -81.4 -84.3 206.2 4.0 39 0.364 SW 133.9 0.036 -185.2 0.33 -78.7 -81.2 145 0.33 -83.4 -82.5 141 0.33 -83.7 -86.9 176.8 4.1 40 0.378 SW 135.5 0.037 -185.3 0.33 -81.4 -83.9 157 0.33 -86.1 -85.3 151 0.33 -86.3 -89.6 185.9 4.3 41 0.371 SW 137.2 0.037 -185.1 0.33 -83.9 -86.5 156 0.33 -88.8 -88 151 0.33 -89 -92.4 197.7 5.9 42 0.364 SW 137.4 0.037 -185.1 0.33 -86.3 -88.9 149 0.33 -91.3 -90.6 147 0.33 -91.5 -95 196 3.4 43 0.351 SW 140.1 0.038 -184.1 0.33 -88.4 -91.2 137 0.33 -93.7 -93 138 0.33 -93.8 -97.6 189.5 4.0 44 0.397 SW 140.3 0.038 -185.1 0.33 -90.9 -93.7 159 0.33 -96.1 -95.5 146 0.33 -96.1 -100 191.4 4.5 45 0.363 SW 143.4 0.038 -185 0.33 -92.9 -95.9 135 0.33 -98.4 -97.9 143 0.33 -98.3 -102.3 181.8 4.9 46 0.378 SW 142.7 0.039 -185.3 0.33 -95.1 -98.1 142 0.33 -101 -100.1 138 0.33 -100 -104.5 181 6.0 47 0.380 SW 145.1 0.039 -185.3 0.33 -97.1 -100.2 137 0.33 -103 -102.4 148 0.33 -103 -106.8 194.3 4.3 48 0.344 SW 147.9 0.04 -185.1 0.33 -100 -103 192 0.33 -105 -105 174 0.33 -105 -109.4 216.3 4.9 49 0.369 SW 148.9 0.04 -185.3 0.33 -102 -105 130 0.33 -107 -107.2 139 0.33 -107 -111.7 195.9 4.9 50 0.360 SW 150.3 0.041 -185.4 0.33 -103 -106.8 120 0.33 -109 -109.2 134 0.33 -109 -113.5 166.3 4.1 51 0.341 SW 153.5 0.042 -185.5 0.33 -105 -108.7 140 0.33 -111 -111 133 0.33 -111 -115.4 182.6 4.0 52 0.324 SW 154.9 0.042 -185.1 0.33 -107 -110.7 141 0.33 -113 -113 138 0.33 -113 -117.5 200 4.9 53 0.373 SW 158.7 0.043 -185.3 0.33 -109 -112.5 136 0.33 -115 -114.9 135 0.33 -114 -119.2 173 4.4 54 0.303 SW 160.2 0.044 -185.2 0.33 -111 -114.3 127 0.33 -117 -116.8 151 0.33 -116 -121.2 203.3 3.8 55 0.376 SW 161.6 0.045 -185.4 0.33 -112 -116 128 0.33 -118 -118.5 119 0.33 -118 -123 187.3 4.2 56 0.340 SW 163.6 0.045 -185.4 0.33 -114 -117.4 111 0.33 -120 -120.1 127 0.33 -119 -124.7 183.7 5.2 57 0.292 SW 164.7 0.046 -185.5 0.33 -115 -119 122 0.33 -122 -121.7 129 0.33 -121 -126.3 176.9 3.4 58 0.307 SW 169.1 0.047 -185.3 0.33 -117 -120.5 122 0.33 -123 -123.1 113 0.33 -122 -127.7 165.5 4.9 59 0.287 SW 171 0.048 -185.3 0.33 -118 -122.1 126 0.33 -125 -124.8 138 0.33 -124 -129.2 184.3 4.5 60 0.314 SW 169.7 0.049 -185.2 0.33 -120 -123.7 133 0.33 -126 -126.4 139 0.33 -125 -130.7 181.6 4.4 61 0.310 SW 172.8 0.049 -185.1 0.33 -121 -124.7 83.4 0.33 -127 -127.7 112 0.33 -126 -132.2 186.8 4.6 62 0.302 SW 176.1 0.051 -185.1 0.33 -122 -126.4 149 0.33 -129 -129.3 155 0.33 -128 -133.8 201.7 4.3 63 0.313
159
EXP 17 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 175.2 0.052 -185.3 0.33 -123 -127.6 102 0.33 -130 -130.6 109 0.33 -129 -135.1 174.8 5.2 64 0.292 SW 174.6 0.052 -185.3 0.33 -125 -129 117 0.33 -131 -131.8 121 0.33 -130 -136.3 174 3.5 65 0.329 SW 176.9 0.053 -185.2 0.33 -126 -130.3 115 0.33 -133 -133.4 155 0.33 -131 -137.5 168 3.6 66 0.309 SW 176.6 0.054 -185.5 0.33 -127 -131.5 113 0.33 -134 -134.4 96.1 0.33 -133 -138.7 189.2 5.7 67 0.328 SW 176.2 0.055 -185.1 0.33 -128 -132.9 133 0.33 -135 -135.6 130 0.33 -134 -139.8 163.4 3.3 68 0.301 SW 176.1 0.056 -185.4 0.33 -130 -134.2 128 0.33 -136 -137 147 0.33 -135 -140.9 179.6 4.1 69 0.361 SW 178.7 0.057 -185.2 0.33 -131 -135.4 114 0.33 -137 -138.2 127 0.33 -136 -142.1 180.4 3.7 70 0.303 SW 174.5 0.058 -185.3 0.33 -132 -136.6 122 0.33 -138 -139.3 127 0.33 -137 -143 152.2 5.5 71 0.350 SW 178.2 0.06 -185.2 0.33 -133 -137.9 128 0.33 -140 -140.5 131 0.33 -138 -144.2 200.7 3.9 72 0.340 SW 178.3 0.062 -185.2 0.33 -134 -139.2 143 0.33 -141 -141.6 128 0.33 -139 -145.3 178.4 5.1 73 0.332 SW 180.2 0.062 -185.1 0.33 -136 -140.4 134 0.33 -142 -142.9 157 0.33 -140 -146.3 182.6 5.7 74 0.310 SW 179.6 0.064 -185 0.33 -137 -141.5 116 0.33 -143 -144.1 151 0.33 -141 -147.4 195.3 4.5 75 0.358 SW 182.6 0.065 -185.3 0.33 -138 -142.5 117 0.33 -144 -145.1 142 0.33 -142 -148.4 177.9 6.1 76 0.389 SW 182.3 0.066 -185.2 0.33 -139 -143.7 135 0.33 -145 -146.2 147 0.33 -143 -149.6 214.6 4.3 77 0.353 SW 184.6 0.067 -185.1 0.33 -140 -144.9 142 0.33 -146 -147.3 144 0.33 -144 -150.5 185.9 5.5 78 0.344 SW 181.9 0.067 -185.1 0.33 -141 -145.8 115 0.33 -147 -148.4 166 0.33 -145 -151.7 218.4 5.9 79 0.371 SW 180.6 0.067 -185 0.33 -142 -147.1 168 0.33 -148 -149.4 138 0.33 -146 -152.5 175.4 4.9 80 0.377 SW 181.4 0.069 -185.5 0.33 -143 -148.2 133 0.33 -149 -150.5 167 0.33 -147 -153.5 200.1 4.2 81 0.387 SW 175.9 0.069 -185.2 0.33 -144 -149.3 143 0.33 -150 -151.5 150 0.33 -147 -154.2 171.1 5.1 82 0.348 SW 180.8 0.071 -185.6 0.33 -145 -149.9 82.1 0.33 -151 -152.3 141 0.33 -148 -155 173.8 6.3 83 0.362 SW 182.5 0.071 -185.1 0.33 -146 -151.3 204 0.33 -152 -153.5 195 0.33 -149 -156 224.6 4.3 84 0.369 SW 179.7 0.073 -185.4 0.33 -147 -152.3 135 0.33 -153 -154.5 172 0.33 -150 -157 216.3 3.2 85 0.374 SW 177.7 0.072 -185.1 0.33 -148 -153.2 139 0.33 -154 -155.5 180 0.33 -151 -158 238.3 3.7 86 0.370 SW 175.3 0.071 -185.4 0.33 -149 -154.3 161 0.33 -155 -156.4 153 0.33 -152 -159 224.7 5.1 87 0.372 SW 181.8 0.073 -185.3 0.42 -150 -155.1 126 0.42 -158 -157.5 69.5 0.17 -170 -175.3 3998 4.3 88 0.391 SW 175.3 0.069 -185.5 0.42 -153 -156.1 107 0.42 -175 -171.2 3143 0.17 -176 -181.5 5182 4.2 89 0.416 SW 171.1 0.069 -185.6 -157.5 -180.9 -182.2 3.7 90 0.405 SW 165.8 0.069 -185.5 -163.5 -183.5 -183.3 5.9 91 0.423 SW 164.9 0.07 -185.5 -176 -184.1 -183.5 4.6 92 0.412 SW 169.2 0.072 -185.6 -182.2 -184.2 -183.6 3.4 93 0.402 SW 179.9 0.08 -185.5 -183.4 -184.7 -184 5.0 94 0.431 SW 182.7 0.087 -185.6 -184.2 -185.3 -184.3 4.8 95 0.390 SW 187.8 0.091 -185.4 -184.3 -185.5 -184.4 4.6 96 0.349 SW 185.2 0.093 -185.3 -184.7 -185.2 -184.5 4.6 97 0.328 SW 183.5 0.094 -185.3 -184.2 -185 -184.3 3.6 98 0.356 SW 184 0.094 -185.6 -184.4 -185.3 -184.5 6.0 99 0.317 SW 184.3 0.095 -185.5 -184.4 -185.3 -184.4 4.9 100 0.285
160
EXP 18 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 52.1 1 12.3 0.33 22.3 23.3 972 0.33 22.3 23.4 927.4 0.33 21.8 23.5 875.8 0.0 1 0.123 N 54 1 11.1 0.33 22.3 22.8 184.2 0.33 22.6 23.1 49.4 0.33 22.1 23.2 33.3 0.0 2 0.213 N 50.1 1 9.7 0.33 22 22.5 188.5 0.33 22.4 22.9 57.1 0.33 21.6 22.9 191.3 0.0 3 0.278 N 56.3 1 8 0.33 21.3 21.8 340.4 0.33 21.6 22.3 270.3 0.33 20.9 22.2 309.2 0.0 4 0.277 N 51.8 1 7.4 0.33 21.2 21.5 132.6 0.33 21.5 22 43.9 0.33 20.7 21.9 161.2 0.0 5 0.157 N 57.9 1 6.1 0.33 20.6 21 231.9 0.33 20.9 21.5 232.1 0.33 20.2 21.4 223 0.0 6 0.304 N 51.7 1 5 0.33 20 20.4 266 0.33 20.3 20.9 209.4 0.33 19.7 20.9 202 0.0 7 0.211 N 54.7 1 3.8 0.33 19.5 19.9 233.7 0.33 19.9 20.4 150.5 0.33 19.3 20.4 189.3 0.0 8 0.244 N 52.4 1 2.5 0.33 18.8 19.1 287.4 0.33 19.1 19.8 223.4 0.33 18.4 19.7 291.8 0.0 9 0.307 N 58.8 1 0.1 0.33 18.3 18.6 210.4 0.33 18.7 19.3 115.6 0.33 18.1 19.1 177.3 0.0 10 0.354 N 54.2 1 -0.8 0.33 17.5 17.8 276.9 0.33 18.1 18.6 186.2 0.33 17.4 18.5 211.7 0.0 11 0.246 N 55.1 1 -2.4 0.33 16.9 17.1 242.6 0.33 17.4 18 158 0.33 16.7 17.8 236.6 0.0 12 0.299 N 53.8 1 -4.3 0.33 16.1 16.3 275.9 0.33 16.7 17.4 141.8 0.33 15.9 17 266.5 0.0 13 0.395 N 57 1 -6.5 0.33 15.5 15.7 204.5 0.33 15.9 16.5 210.1 0.33 15.2 16.3 208.6 0.0 14 0.377 N 57.9 1 -8.4 0.33 14.8 14.9 213.4 0.33 15.1 15.8 164.6 0.33 14.4 15.5 231.8 0.0 15 0.367 N 57 1 -10.9 0.33 13.9 14 258.2 0.33 14.4 15 147.7 0.33 13.7 14.7 201.6 0.0 16 0.413 N 57.9 1 -13.1 0.33 12.9 13 259 0.33 13.4 14.1 164.9 0.33 12.4 13.5 297.2 0.0 17 0.378 N 58.9 1 -16.8 0.33 11.8 11.9 256.4 0.33 12.5 13.1 162.3 0.33 11.7 12.6 203.4 0.0 18 0.382 N 58.1 1 -19.5 0.33 10.7 10.8 251.9 0.33 11.5 12.1 168.8 0.33 10.8 11.7 209.7 0.0 19 0.398 N 59.4 1 -22.7 0.33 9.7 9.7 179.3 0.33 10.3 11 136.7 0.33 9.4 10.4 205.4 0.0 20 0.407 N 61.6 1 -36.8 0.33 8.4 8.4 195.5 0.33 9 9.7 150.4 0.33 8.2 9.1 195.1 0.0 21 0.41 N 60.5 1 -39.7 0.33 6.9 6.9 244.5 0.33 7.4 8.3 161.6 0.33 6.3 7.3 275.6 0.0 22 0.412 N 60.7 1 -40.8 0.33 5.7 5.5 196.4 0.33 6.3 7.1 124.8 0.33 5.1 5.9 208.9 0.0 23 0.414 N 61.2 1 -43.3 0.33 3.9 3.8 317.6 0.33 4.6 5.5 210.1 0.33 3.5 4.2 296.5 0.0 24 0.413 N 59.4 1 -37.9 0.33 2.6 2.3 233.5 0.33 3.1 3.9 189.8 0.33 2 2.7 258.5 0.0 25 0.41 N 61.9 1 -41.6 0.33 0.9 0.6 299.3 0.33 1.6 2.4 185.7 0.33 0.7 1.2 258.1 0.0 26 0.374 N 58.7 1 -41.8 0.33 -0.6 -1 231.4 0.33 -0.1 0.7 196.3 0.33 -1 -0.4 242.4 0.0 27 0.412 N 59.7 1 -50.8 0.33 -1.7 -2.2 137.7 0.33 -1.3 -0.6 95.9 0.33 -2.3 -1.9 161.2 0.0 28 0.388 N 61.4 1 -69.8 0.33 -3.4 -3.9 159.5 0.33 -3.4 -2.3 121.9 0.33 -4.8 -4.2 225.4 0.0 29 0.377 N 61.7 1 -82 0.33 -5.3 -5.7 155.2 0.33 -5.5 -4.3 136.8 0.33 -6.8 -6.4 193.7 0.0 30 0.37 N 62.7 1 -90.8 0.33 -7.1 -7.5 149.1 0.33 -7.6 -6.3 121.4 0.33 -9.4 -8.9 219.4 0.0 31 0.353 N 64.7 1 -97.1 0.33 -8.9 -9.3 142.3 0.33 -10 -8.4 132.6 0.33 -12.1 -11.7 234.6 0.0 32 0.382 N 64.3 1 -100.7 0.33 -10.6 -11.1 135 0.33 -11.9 -10.3 105.1 0.33 -14.4 -14.2 205.2 0.0 33 0.344 N 66.5 1 -105.9 0.33 -12.7 -13.1 151.2 0.33 -14.6 -12.7 146.6 0.33 -17.1 -17 230.7 0.0 34 0.314 N 65.8 1 -108.7 0.33 -14.4 -14.9 126.2 0.33 -16.6 -14.8 116.5 0.33 -19.3 -19.4 200.5 0.0 35 0.337 N 67.7 1 -113.5 0.33 -16.5 -16.9 136.4 0.33 -19.3 -17.2 139.9 0.33 -22.2 -22.3 235.6 0.0 36 0.331 N 67.4 1 -116.8 0.33 -18.4 -18.9 139.7 0.33 -21.4 -19.4 124.3 0.33 -24.4 -24.8 217.6 0.0 37 0.343 N 70.2 1 -114.9 0.33 -20.3 -20.8 136.4 0.33 -23.7 -21.5 118.1 0.33 -27.2 -27.6 249.9 0.0 38 0.32
161
EXP 18 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 68.1 1 -116 0.33 -22.3 -22.8 150 0.33 -25.8 -23.7 127.6 0.33 -29.1 -29.8 209.9 0.0 39 0.317
SW 70.2 0.036 -114.6 0.33 -24.2 -24.8 141.1 0.33 -28.2 -25.9 124.9 0.33 -31.9 -32.5 264.4 2.7 40 0.3 SW 68.5 0.036 -115.7 0.33 -25.9 -26.5 118.2 0.33 -30.5 -28.1 139.8 0.33 -34 -34.9 229 1.9 41 0.326 SW 71.7 0.035 -119.1 0.33 -28.1 -28.6 151.1 0.33 -32.7 -30.3 120 0.33 -36.5 -37.5 244.4 2.0 42 0.321 SW 71.5 0.035 -122.1 0.33 -29.8 -30.5 118.7 0.33 -34.8 -32.4 115.3 0.33 -38.6 -39.8 218.3 2.7 43 0.3 SW 72.3 0.035 -128 0.33 -31.8 -32.4 134 0.33 -37.1 -34.7 139.3 0.33 -40.9 -42.1 231.4 3.7 44 0.284 SW 69.2 0.036 -125.7 0.33 -33.8 -34.4 136.4 0.33 -39.1 -36.7 118.3 0.33 -42.8 -44.3 217 2.8 45 0.31 SW 70.2 0.036 -127.3 0.33 -35.6 -36.4 130.2 0.33 -41.2 -38.8 112.2 0.33 -45 -46.5 229.8 2.9 46 0.319 SW 71.2 0.035 -129.4 0.33 -37.6 -38.4 103.4 0.33 -43.5 -41 104.9 0.33 -47.3 -48.9 175.6 3.3 47 0.327 SW 70.3 0.036 -158.5 0.33 -39.3 -40.1 76.3 0.33 -45.4 -43 78.3 0.33 -49.3 -51 147.8 3.7 48 0.266 SW 68.3 0.036 -175.9 0.33 -41.3 -42.1 93.3 0.33 -47.5 -45.1 85.1 0.33 -51.1 -53.1 138.9 4.3 49 0.35 SW 65.7 0.037 -176.5 0.33 -43.1 -44 84.5 0.33 -49.1 -47 73.1 0.33 -52.5 -54.6 116.5 3.7 50 0.323 SW 63.8 0.038 -176.2 0.33 -44.8 -45.8 82 0.33 -50.8 -48.8 74.6 0.33 -54 -56.2 122 5.1 51 0.317 SW 64.4 0.037 -176.6 0.33 -46.5 -47.5 79.7 0.33 -52.9 -50.8 88.9 0.33 -56 -58.1 138.2 3.1 52 0.315 SW 67.3 0.036 -176.3 0.33 -48.2 -49.3 83.6 0.33 -54.5 -52.4 64.7 0.33 -57.8 -60.1 141.1 3.7 53 0.215 SW 64.6 0.037 -176.6 0.33 -49.9 -51.1 83.4 0.33 -56.1 -54.1 71.1 0.33 -59.4 -61.8 132.9 4.1 54 0.2 SW 65.3 0.037 -177 0.33 -51.3 -52.6 70.5 0.33 -57.7 -55.8 73.3 0.33 -60.8 -63.3 118.5 3.3 55 0.267 SW 67.2 0.036 -177.1 0.33 -53 -54.3 79.5 0.33 -59.5 -57.6 82.7 0.33 -62.4 -65 131.8 2.7 56 0.222 SW 63.3 0.038 -177.6 0.33 -54.5 -55.9 75.4 0.33 -61.1 -59.2 67.4 0.33 -64.3 -66.9 143.5 3.1 57 0.228 SW 64.4 0.037 -177.5 0.33 -56 -57.5 73 0.33 -62.7 -60.9 77.6 0.33 -65.5 -68.3 115.6 3.2 58 0.206 SW 66.2 0.036 -177.3 0.33 -57.5 -59 75.6 0.33 -64.2 -62.4 64.3 0.33 -67.2 -70 136.8 3.2 59 0.195 SW 64.1 0.037 -177.7 0.33 -59 -60.6 73.8 0.33 -65.6 -63.9 66.1 0.33 -68.5 -71.5 126.6 3.7 60 0.189 SW 64.8 0.037 -177.8 0.33 -60.5 -62.1 74.2 0.33 -67.3 -65.6 76.5 0.33 -70.2 -73.1 136 4.3 61 0.202 SW 62.4 0.038 -178.4 0.33 -61.7 -63.4 62.2 0.33 -68.5 -66.9 57.3 0.33 -71.4 -74.6 124.5 3.8 62 0.198 SW 64.9 0.037 -177.8 0.33 -63.3 -64.9 76.7 0.33 -70.4 -68.6 88.9 0.33 -73.1 -76.2 140.5 3.5 63 0.176 SW 66 0.036 -178.3 0.33 -64.4 -66.1 57.1 0.33 -71.6 -70 63.1 0.33 -74.4 -77.6 127.2 2.9 64 0.144 SW 67.2 0.036 -177.8 0.33 -65.6 -67.4 58.1 0.33 -73.3 -71.5 74.2 0.33 -76.2 -79.4 155.1 3.6 65 0.148 SW 72.6 0.034 -178.3 0.33 -66.8 -68.6 60.3 0.33 -74.4 -72.7 57.9 0.33 -77.4 -80.9 130.4 3.6 66 0.151 SW 81.3 0.032 -177.9 0.33 -68.3 -70.1 74.7 0.33 -76.1 -74.2 68.5 0.33 -79.5 -82.8 174.2 3.8 67 0.166 SW 78.4 0.033 -178.2 0.33 -69.5 -71.3 60.8 0.33 -77.8 -75.8 88.5 0.33 -81.1 -84.6 157.9 3.2 68 0.178 SW 83 0.032 -177.7 0.33 -70.7 -72.6 59.8 0.33 -79.3 -77.2 66.3 0.33 -82.8 -86.4 169.8 4.0 69 0.163 SW 81 0.033 -178.8 0.33 -72.1 -73.9 67.7 0.33 -80.9 -78.7 73.1 0.33 -84.8 -88.4 182.6 3.8 70 0.164 SW 79.4 0.033 -178.8 0.33 -73.2 -75.1 56.7 0.33 -82.2 -80.1 67.9 0.33 -86 -89.9 153.2 2.9 71 0.195 SW 89.9 0.031 -178.6 0.33 -74.4 -76.3 53.3 0.33 -83.6 -81.5 67.4 0.33 -87.5 -91.4 165.5 3.5 72 0.193 SW 85.9 0.032 -178.4 0.33 -75.7 -77.6 64.2 0.33 -85.1 -82.9 75.6 0.33 -89 -93 165.3 2.9 73 0.196 SW 91.9 0.031 -178.2 0.33 -76.5 -78.5 37.9 0.33 -86.6 -84.3 73.3 0.33 -90.6 -94.6 176 3.7 74 0.166 SW 78.9 0.033 -178.5 0.33 -78.1 -79.9 75.2 0.33 -87.9 -85.7 71.8 0.33 -91.8 -96 162 2.6 75 0.192 SW 98 0.03 -178.2 0.33 -79.3 -81.2 62.5 0.33 -89.4 -87.1 77 0.33 -93.5 -97.6 182.6 3.3 76 0.149
162
EXP 18 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 88 0.032 -178.9 0.33 -80.4 -82.4 57.7 0.33 -90.4 -88.1 44 0.33 -94.6 -99 162 2.6 77 0.23 SW 82.6 0.033 -178.5 0.33 -81.4 -83.5 48 0.33 -91.6 -89.3 62.5 0.33 -95.9 -100.3 172.4 3.1 78 0.168 SW 108.1 0.03 -177.9 0.33 -82.7 -84.7 58.9 0.33 -93.4 -90.8 79.7 0.33 -97.9 -102.2 217.9 2.3 79 0.155 SW 81.4 0.034 -179 0.33 -83.6 -85.7 47.8 0.33 -94.1 -91.8 42.9 0.33 -98.5 -103.2 146 3.3 80 0.228 SW 100.6 0.03 -177.9 0.33 -84.8 -86.8 53.5 0.33 -95.7 -93.2 77.5 0.33 -100.4 -104.9 214.4 2.1 81 0.108 SW 101.1 0.031 -178.2 0.33 -86 -88.1 64.6 0.33 -96.8 -94.3 54.1 0.33 -101.4 -106.2 177.5 2.2 82 0.218 SW 104.1 0.031 -177.7 0.33 -87.2 -89.3 60.7 0.33 -98.1 -95.6 69.3 0.33 -102.7 -107.5 192.5 3.5 83 0.161 SW 91.4 0.033 -178.3 0.33 -88.4 -90.5 61.8 0.33 -99.4 -97 76.2 0.33 -103.8 -108.7 175.6 2.0 84 0.242 SW 93.5 0.032 -178.6 0.33 -89.3 -91.6 48.8 0.33 -100.3 -98 46.6 0.33 -104.9 -109.9 183.5 2.1 85 0.164 SW 98.4 0.031 -178.2 0.33 -90.5 -92.7 57.1 0.33 -101.7 -99.3 75.6 0.33 -106.1 -111.1 189.6 2.4 86 0.137 SW 100.3 0.031 -178 0.33 -91.6 -93.9 57.5 0.33 -102.8 -100.4 58.9 0.33 -107.5 -112.5 210.3 2.2 87 0.176 SW 96.8 0.032 -178.1 0.33 -92.9 -95.2 68.5 0.33 -104.2 -101.8 88.1 0.33 -108.5 -113.6 184 4.8 88 0.168 SW 104.5 0.031 -178.8 0.33 -93.6 -96 38.1 0.33 -104.8 -102.6 33.7 0.33 -109.2 -114.5 168.7 2.6 89 0.223 SW 95.2 0.032 -178 0.33 -94.7 -97.1 51.3 0.33 -106.1 -103.8 70.8 0.33 -110.5 -115.7 200.7 2.2 90 0.17 SW 108 0.031 -178.2 0.33 -95.6 -98 45.4 0.33 -107.2 -105 75.7 0.33 -111.4 -116.7 180.3 5.5 91 0.202 SW 98.5 0.032 -178.3 0.33 -97 -99.4 78.4 0.33 -108.4 -106.1 66.1 0.33 -112.6 -117.9 210.5 3.2 92 0.171 SW 105.2 0.031 -177.9 0.33 -97.9 -100.3 42.3 0.33 -109.5 -107.4 87.4 0.33 -113.3 -118.8 171.8 3.2 93 0.197 SW 89.9 0.033 -178.2 0.33 -99 -101.6 69.8 0.33 -110.2 -108 22.9 0.33 -114.4 -119.9 201.7 2.3 94 0.099 SW 104.4 0.032 -178.2 0.33 -100 -102.6 54.9 0.33 -111.1 -109 58.1 0.33 -115.3 -120.8 187.8 2.4 95 0.187 SW 99.2 0.032 -178.2 0.33 -100.8 -103.5 43.7 0.33 -112.3 -110.2 73 0.33 -116.4 -122 210.5 6.2 96 0.16 SW 106.7 0.032 -178.4 0.33 -101.8 -104.5 56.7 0.33 -113.1 -111 42.5 0.33 -117.3 -122.9 197.9 2.6 97 0.211 SW 105.2 0.032 -177.8 0.33 -102.9 -105.6 60.1 0.33 -114.4 -112.2 83 0.33 -118.5 -124.1 226.2 3.2 98 0.166 SW 110.1 0.031 -178 0.33 -103.7 -106.6 50.4 0.33 -115 -112.9 26.7 0.33 -119.3 -125 197.7 5.2 99 0.141 SW 100.6 0.032 -178.4 0.33 -104.7 -107.5 54.2 0.33 -116.1 -114 73.6 0.33 -120.2 -126 209.9 2.7 100 0.202 SW 113.9 0.031 -177.8 0.33 -105.4 -108.4 44.2 0.33 -117.1 -115 56.1 0.33 -121.3 -127.1 234.5 3.0 101 0.206 SW 108.8 0.032 -177.6 0.33 -106.8 -109.7 83.3 0.33 -118 -116 67.8 0.33 -121.9 -127.8 190.8 2.9 102 0.188 SW 98.2 0.032 -177.7 0.33 -107.5 -110.6 50.7 0.33 -118.8 -116.9 56.3 0.33 -122.5 -128.5 187.4 4.1 103 0.171 SW 125.4 0.03 -177.2 0.33 -108.7 -111.7 69.8 0.33 -120 -118.2 92.4 0.33 -123.6 -129.5 222.1 5.6 104 0.228 SW 87.3 0.035 -178.2 0.33 -109.7 -112.8 66 0.33 -120.9 -119.2 74.1 0.33 -124.1 -130.2 189.6 3.6 105 0.23 SW 101.4 0.031 -177.8 0.33 -110.7 -113.8 66.7 0.33 -121.7 -120.1 62.7 0.33 -125 -131.1 209.3 4.1 106 0.142 SW 91.6 0.033 -178.6 0.33 -111.4 -114.6 40.8 0.33 -122.3 -120.9 62.4 0.33 -125.1 -131.3 136.1 6.1 107 0.203 SW 95.3 0.032 -178.4 0.33 -112.7 -115.8 83.8 0.33 -123.5 -122 87.2 0.33 -126.3 -132.3 230.2 3.8 108 0.179 SW 98.6 0.032 -178.4 0.33 -113.4 -116.8 59.9 0.33 -124 -122.6 26.9 0.33 -127 -133.2 202.5 3.9 109 0.159 SW 100 0.032 -178.8 0.33 -114 -117.5 36.4 0.33 -124.7 -123.4 64.5 0.33 -127.5 -133.8 180.7 5.6 110 0.177 SW 93.3 0.033 -178.9 0.33 -115.1 -118.5 71.6 0.33 -125.8 -124.4 80.4 0.33 -128.5 -134.6 218.3 2.9 111 0.142 SW 98.8 0.032 -179 0.33 -115.7 -119.2 43.4 0.33 -126.2 -125 35.6 0.33 -129 -135.3 190.2 6.0 112 0.131 SW 106.8 0.031 -179.3 0.33 -116.4 -119.9 40.8 0.33 -127.1 -125.8 57.4 0.33 -130 -136.2 222.9 6.2 113 0.119 SW 93.4 0.033 -179.3 0.33 -117.4 -121 77.5 0.33 -127.9 -126.6 62.9 0.33 -130.5 -136.9 200.2 4.4 114 0.128
163
EXP 18 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 106.4 0.031 -179 0.33 -117.8 -121.5 24 0.33 -128.4 -127.1 17.7 0.33 -131.5 -137.8 236.7 4.7 115 0.172 SW 109.4 0.032 -179.5 0.33 -118.8 -122.4 70.9 0.33 -129.3 -128 67.1 0.33 -132.2 -138.6 216.6 5.1 116 0.115 SW 106.3 0.032 -179.9 0.33 -119.3 -123.2 47.4 0.33 -129.5 -128.5 19.6 0.33 -132.2 -138.8 155.8 4.3 117 0.217 SW 104.9 0.032 -178.5 0.33 -120.3 -124.1 69.5 0.33 -130.7 -129.4 67.2 0.33 -133.6 -139.9 278.2 6.5 118 0.223 SW 122.7 0.031 -179.6 0.33 -120.5 -124.5 14 0.33 -131.2 -130 39.8 0.33 -134 -140.5 201.4 5.1 119 0.233 SW 85.2 0.036 -180.1 0.33 -121.1 -125 31.1 0.33 -131.6 -130.6 44.6 0.33 -134.2 -140.8 165 5.0 120 0.132 SW 101.7 0.032 -179.7 0.33 -122.2 -126 84 0.33 -132.6 -131.3 52 0.33 -135.5 -141.9 286 3.8 121 0.088 SW 109.2 0.032 -179.8 0.33 -122.7 -126.6 42 0.33 -133.4 -132.1 44.4 0.33 -136.7 -143.1 296.9 5.6 122 0.15 SW 101.3 0.033 -180.3 0.33 -123 -127 19.1 0.33 -133.7 -132.5 16.3 0.33 -136.8 -143.6 198.2 3.5 123 0.122 SW 113.2 0.032 -179.7 0.33 -124 -127.9 70.8 0.33 -134.5 -133.4 73.4 0.33 -137 -143.8 170.3 3.5 124 0.137 SW 110.8 0.033 -180.5 0.33 -124.6 -128.5 39.8 0.33 -135.7 -134.3 89.5 0.33 -138.5 -145 327.6 3.2 125 0.169 SW 99.2 0.033 -180.1 0.33 -125.6 -129.6 92.1 0.33 -135.9 -135 38.2 0.33 -138.3 -145.2 164.4 4.5 126 0.161 SW 117.4 0.032 -179.8 0.33 -125.7 -129.9 8.5 0.33 -136.3 -135.3 6.3 0.33 -139 -145.8 233.2 4.9 127 0.175 SW 96.6 0.035 -180.4 0.33 -126.2 -130.3 22.5 0.33 -137.3 -136.1 80.9 0.33 -139.9 -146.7 272.9 3.5 128 0.13 SW 97.8 0.034 -180.3 0.33 -126.9 -131 56.8 0.33 -137.2 -136.5 15.2 0.33 -139.3 -146.4 96.7 4.2 129 0.113 SW 98 0.033 -180 0.33 -127.5 -131.7 50.3 0.33 -137.9 -136.9 24.9 0.33 -140.4 -147.2 281 3.4 130 0.136 SW 100.2 0.034 -179.8 0.33 -128.2 -132.3 43.4 0.33 -139.2 -138.1 128.4 0.33 -141.6 -148.3 318.3 4.9 131 0.162 SW 110.6 0.034 -180.6 0.33 -128.7 -132.8 40.4 0.33 -139.2 -138.4 11.6 0.33 -141.3 -148.4 149.9 4.1 132 0.142 SW 95 0.034 -180.7 0.42 -130.3 -134.2 133.7 0.42 -141.3 -139.6 119.2 0.17 -149.4 -155.4 1562.9 7.8 133 0.138 SW 89.2 0.035 -180.4 0.42 -132.1 -135.3 87.8 0.42 -151.7 -145.9 965 0.17 -170.9 -175 5418.9 4.8 134 0.063 SW 101.1 0.033 -180 -135.1 -154.5 -176.5 4.1 135 0.075 SW 99.4 0.033 -180.1 -136.5 -160.9 -176.3 3.4 136 0.168 SW 105.5 0.033 -180 -137.5 -164.4 -176.4 4.1 137 0.164 SW 91.9 0.036 -180.5 -140.4 -167.5 -176.7 5.8 138 0.106 SW 96.5 0.033 -180.4 -142.6 -170.4 -177.7 4.7 139 0.093 SW 101.5 0.033 -180.4 -145.3 -172.5 -177.5 5.2 140 0.129 SW 102.9 0.034 -180.6 -147.5 -172.3 -177.1 4.8 141 0.089 SW 104.9 0.035 -180.2 -150.5 -174.6 -178.4 4.4 142 0.105 SW 96.5 0.035 -180.3 -152 -174.7 -178 4.0 143 0.175 SW 116.6 0.034 -180.4 -155.4 -176 -178.1 5.4 144 0.214 SW 94.9 0.037 -180.5 -158 -177.4 -178.1 4.2 145 0.07 SW 103.5 0.035 -180.4 -160.3 -177.1 -178.5 4.6 146 0.144 SW 111.8 0.035 -180.8 -162.2 -176.7 -178.1 4.0 147 0.149 SW 98.5 0.036 -181 -164.1 -177.3 -178.2 4.6 148 0.157 SW 107.2 0.037 -180.7 -166.5 -177.8 -178.5 6.7 149 0.197 SW 112.4 0.04 -181 -168 -178.3 -179.1 4.4 150 0.21 SW 119.3 0.039 -181.2 -170.2 -178.8 -179 4.7 151 0.201 SW 114.2 0.04 -181.7 -170.7 -178.3 -178.4 4.2 152 0.135
164
EXP 18 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 102.7 0.036 -181.2 -176.3 -180.7 -179.5 5.7 153 0.072 SW 100.6 0.036 -181.4 -178 -180.8 -180.4 3.9 154 0.186
EXP 19 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P N 53.3 1 12.2 0.33 22.31 23 609 0.33 22.88 23.4 287 0.33 22.38 23.6 189.8 0.0 1 0.216 N 53.4 1 10.8 0.33 21.87 22.4 294 0.33 22.34 22.9 231 0.33 21.78 23.1 267.6 0.0 2 0.285 N 57 1 8.4 0.33 21.39 21.8 275 0.33 21.93 22.4 202 0.33 21.44 22.7 175.8 0.0 3 0.304 N 56.8 1 7.4 0.33 20.84 21.3 261 0.33 21.23 21.7 325 0.33 20.86 22.1 244.2 0.0 4 0.229 N 57.3 1 6.6 0.33 19.99 20.4 442 0.33 20.71 21.2 186 0.33 20.24 21.5 269.5 0.0 5 0.197 N 58.9 1 5.5 0.33 19.84 20.1 137 0.33 20.28 20.8 142 0.33 19.67 20.9 251.4 0.0 6 0.269 N 55.6 1 4.3 0.33 18.62 19.1 495 0.33 19.29 19.9 380 0.33 18.9 20.1 301.5 0.0 7 0.233 N 57.1 1 3.1 0.33 18.1 18.4 300 0.33 18.83 19.3 203 0.33 18.49 19.6 191.1 0.0 8 0.303 N 58.9 1 1.6 0.33 17.76 17.9 204 0.33 18.5 18.9 92.6 0.33 18.05 19.1 172.7 0.0 9 0.284 N 56.6 1 0.2 0.33 16.84 17.1 317 0.33 17.37 18 326 0.33 16.96 18.2 340.2 0.0 10 0.259 N 56.2 1 -1.8 0.33 15.69 15.9 451 0.33 16.56 17.1 231 0.33 16.09 17.2 303.4 0.0 11 0.339 N 59.4 1 -3.7 0.33 15.22 15.3 206 0.33 15.79 16.3 255 0.33 15.45 16.5 227.1 0.0 12 0.368 N 59.1 0.428 -5.4 0.33 14 14.2 408 0.33 14.77 15.3 291 0.33 14.51 15.6 287.4 0.0 13 0.309 N 59.3 0.249 -6.8 0.33 13.41 13.5 262 0.33 14.1 14.6 180 0.33 13.72 14.7 257.2 0.0 14 0.331 N 57.6 0.178 -8.2 0.33 12.51 12.5 320 0.33 13.36 13.8 187 0.33 13.01 14 223.7 0.0 15 0.342 N 59.7 0.127 -9.6 0.33 11.63 11.6 286 0.33 12.33 12.8 263 0.33 12.06 13 264.4 0.0 16 0.39 N 60.5 0.096 -11.7 0.33 10.58 10.6 324 0.33 11.34 11.8 266 0.33 11.22 12.1 237.7 0.0 17 0.417 N 60.5 0.076 -13.7 0.33 9.749 9.7 249 0.33 10.33 10.8 222 0.33 10.13 11 268.4 0.0 18 0.417 N 59.8 0.054 -17 0.33 8.481 8.5 324 0.33 9.283 9.7 215 0.33 9.122 10 236.1 0.0 19 0.415 N 60.3 0.054 -20.7 0.33 7.354 7.2 197 0.33 8.248 8.7 118 0.33 7.958 8.8 168.8 0.0 20 0.414 N 62.4 0.129 -40.3 0.33 5.602 5.6 240 0.33 6.128 6.9 248 0.33 5.911 6.9 264.7 0.0 21 0.418 N 62.8 0.078 -43.5 0.33 4.077 4 232 0.33 4.433 5.2 193 0.33 3.996 5 267.6 0.0 22 0.407 N 62.7 0.069 -46.7 0.33 2.119 2.1 267 0.33 2.608 3.4 207 0.33 2.228 3.1 239.8 0.0 23 0.421 N 62.8 0.064 -51.4 0.33 0.213 0.1 326 0.33 0.703 1.6 236 0.33 0.171 1 322 0.0 24 0.408 N 62.4 0.059 -44.5 0.33 -1.19 -1.6 267 0.33 -0.66 0 197 0.33 -1.1 -0.6 237.1 0.0 25 0.393 N 62.4 0.055 -45.2 0.33 -2.91 -3.4 302 0.33 -2.26 -1.6 203 0.33 -2.69 -2.2 261 0.0 26 0.405 N 62.4 0.052 -46.7 0.33 -4.43 -5 212 0.33 -3.91 -3.2 158 0.33 -4.4 -4 216.1 0.0 27 0.422
SW 63.7 0.044 -62 0.33 -6.36 -6.9 197 0.33 -5.97 -5.2 170 0.33 -6.35 -5.9 195.8 2.2 28 0.408 SW 63.6 0.044 -77.5 0.33 -8.48 -8.9 184 0.33 -8.6 -7.4 162 0.33 -9.37 -8.8 247 1.8 29 0.404 SW 64.9 0.043 -91.5 0.33 -10.5 -11.1 172 0.33 -10.9 -9.6 139 0.33 -11.8 -11.4 211.2 1.6 30 0.399 SW 67.8 0.042 -100.4 0.33 -12.5 -13.1 153 0.33 -13.6 -12 144 0.33 -15 -14.6 243.6 2.2 31 0.367
165
EXP 19 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 70.6 0.04 -106.9 0.33 -14.9 -15.4 167 0.33 -16.3 -14.5 142 0.33 -18 -17.7 231.4 2.2 32 0.371 SW 71.6 0.04 -114.8 0.33 -17.3 -17.8 173 0.33 -19.2 -17.3 153 0.33 -21.3 -21.1 249.6 2.1 33 0.341 SW 72.8 0.039 -117.6 0.33 -19.3 -19.9 141 0.33 -21.9 -19.8 130 0.33 -24.4 -24.4 246.8 2.9 34 0.373 SW 76.7 0.038 -122.3 0.33 -21.5 -22.1 144 0.33 -24.6 -22.4 136 0.33 -27.3 -27.6 230 2.4 35 0.327 SW 77.5 0.038 -127 0.33 -23.8 -24.4 152 0.33 -27.3 -24.9 138 0.33 -30.1 -30.5 234.6 2.6 36 0.345 SW 76.1 0.038 -125 0.33 -26.1 -26.7 157 0.33 -30.1 -27.6 136 0.33 -33.3 -33.8 255.1 2.6 37 0.331 SW 75.3 0.039 -128.4 0.33 -28.4 -29 151 0.33 -32.7 -30.1 136 0.33 -35.9 -36.7 232.3 4.0 38 0.321 SW 76.4 0.038 -129.6 0.33 -30.5 -31.2 100 0.33 -35.1 -32.6 91.7 0.33 -38.4 -39.4 153.4 4.0 39 0.336 SW 79.6 0.037 -174.9 0.33 -32.8 -33.5 107 0.33 -37.8 -35.1 93 0.33 -41.3 -42.3 173.6 4.7 40 0.296 SW 79.7 0.037 -174.7 0.33 -35.1 -35.9 112 0.33 -40.2 -37.5 84.6 0.33 -43.8 -45 161.9 3.0 41 0.343 SW 77.8 0.038 -175 0.33 -37.1 -38 99.3 0.33 -42.3 -39.7 78.6 0.33 -46 -47.5 151.3 3.1 42 0.355 SW 75.7 0.038 -174.9 0.33 -39.4 -40.3 109 0.33 -45 -42.2 97.2 0.33 -48.6 -50.1 168.2 3.6 43 0.378 SW 74.5 0.039 -175.5 0.33 -41.6 -42.6 109 0.33 -47.3 -44.7 92.2 0.33 -50.9 -52.6 160.1 4.4 44 0.342 SW 74 0.039 -175.4 0.33 -43.5 -44.6 98.8 0.33 -49.2 -46.8 77.1 0.33 -52.6 -54.6 135.7 3.1 45 0.414 SW 72.4 0.039 -175.8 0.33 -45.9 -46.9 112 0.33 -51.8 -49.3 104 0.33 -55.1 -57 164.9 2.8 46 0.397 SW 69.4 0.04 -176 0.33 -47.7 -49 101 0.33 -53.7 -51.3 71.7 0.33 -57.1 -59.3 151.8 3.5 47 0.419 SW 69.9 0.04 -176.3 0.33 -49.5 -50.9 93.5 0.33 -55.5 -53.2 74.4 0.33 -58.8 -61.1 133.4 4.0 48 0.374 SW 72.4 0.039 -175.8 0.33 -51.9 -53.1 112 0.33 -58 -55.7 110 0.33 -61 -63.3 158.1 4.0 49 0.379 SW 73.7 0.039 -176.1 0.33 -53.4 -55 90.6 0.33 -59.6 -57.4 58.5 0.33 -62.8 -65.3 147.8 4.1 50 0.365 SW 71.5 0.039 -176.5 0.33 -55.2 -56.8 89.6 0.33 -61.7 -59.5 90.8 0.33 -64.8 -67.3 150.5 3.9 51 0.296 SW 71.1 0.04 -176.8 0.33 -57.2 -58.7 102 0.33 -63.6 -61.4 79 0.33 -66.7 -69.4 153.6 3.1 52 0.256 SW 68.2 0.041 -177.1 0.33 -58.9 -60.5 93.3 0.33 -65.5 -63.3 74.6 0.33 -68.7 -71.4 157.5 2.2 53 0.249 SW 75.1 0.038 -177.3 0.33 -60.2 -62 73.7 0.33 -67.2 -65 69.8 0.33 -70.4 -73.3 149.6 4.4 54 0.225 SW 75.1 0.038 -177.6 0.33 -62.1 -63.8 94.4 0.33 -69.2 -66.9 75.7 0.33 -72.6 -75.5 171.5 3.5 55 0.216 SW 79 0.037 -177.6 0.33 -63.6 -65.4 83 0.33 -71 -68.7 77.8 0.33 -74.3 -77.4 155.5 3.8 56 0.212 SW 83.2 0.037 -177.9 0.33 -65 -66.9 73.5 0.33 -72.6 -70.3 63 0.33 -76.1 -79.3 161.6 5.0 57 0.247 SW 89.7 0.036 -177.8 0.33 -66.5 -68.5 83.7 0.33 -74.5 -71.9 63.5 0.33 -78.3 -81.5 182.9 3.6 58 0.175 SW 82 0.037 -178 0.33 -68.1 -70 81.8 0.33 -76.4 -73.8 74.4 0.33 -80.4 -83.7 188.1 4.4 59 0.21 SW 86.1 0.036 -178 0.33 -69.2 -71.2 62.3 0.33 -77.7 -75.2 48.2 0.33 -81.7 -85.3 152 3.1 60 0.17 SW 90.7 0.036 -177.9 0.33 -70.8 -72.8 82.6 0.33 -79.6 -76.9 69.7 0.33 -83.8 -87.3 189.2 1.4 61 0.179 SW 92.8 0.036 -177.5 0.33 -72.5 -74.5 91.4 0.33 -81.7 -78.8 82.7 0.33 -86 -89.6 208.2 2.3 62 0.183 SW 104.4 0.034 -177.3 0.33 -73.8 -75.9 74 0.33 -83.2 -80.2 47.9 0.33 -88 -91.7 203.4 2.5 63 0.204 SW 101.2 0.035 -176.9 0.33 -75 -77 60.5 0.33 -85 -81.9 67.6 0.33 -89.9 -93.7 205.4 2.9 64 0.217 SW 109.6 0.035 -176.5 0.33 -76.7 -78.7 94.3 0.33 -86.8 -83.6 65.4 0.33 -91.9 -95.8 218.4 3.6 65 0.189 SW 108.7 0.035 -176.9 0.33 -78.1 -80.2 81.6 0.33 -88.4 -85.2 59.2 0.33 -93.7 -97.8 215.2 3.8 66 0.262 SW 109.9 0.035 -176.8 0.33 -79.3 -81.5 69 0.33 -90 -86.6 47.8 0.33 -95.6 -99.8 222.7 3.6 67 0.191 SW 124.8 0.035 -176.7 0.33 -80.7 -82.9 74 0.33 -92 -88.3 57.5 0.33 -98 -102.2 262 1.8 68 0.222 SW 107.8 0.037 -176.9 0.33 -82.3 -84.5 90.7 0.33 -93.5 -89.9 58.3 0.33 -99.5 -104 220.5 3.3 69 0.223
166
EXP 19 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 111.1 0.036 -177.3 0.33 -83.5 -85.8 74.2 0.33 -94.7 -91.3 44.6 0.33 -100 -105.2 180.2 2.8 70 0.193 SW 125.3 0.036 -176.7 0.33 -84.8 -87.1 73.5 0.33 -96.5 -92.8 50.8 0.33 -103 -107.2 256.9 2.1 71 0.232 SW 122.6 0.037 -176.6 0.33 -86.2 -88.5 76 0.33 -97.8 -94.3 57.8 0.33 -104 -108.6 202 3.0 72 0.244 SW 106.5 0.038 -176.9 0.33 -87.7 -90 88.8 0.33 -99.3 -95.8 56.2 0.33 -105 -110 218 5.8 73 0.179 SW 121.9 0.037 -176.4 0.33 -88.5 -91 53.4 0.33 -100 -97 34.5 0.33 -106 -111 178.1 3.1 74 0.194 SW 119.9 0.038 -177 0.33 -90.5 -92.7 105 0.33 -103 -98.9 93.7 0.33 -108 -113.1 291.5 2.9 75 0.211 SW 111.9 0.038 -176.9 0.33 -91.3 -93.8 54.5 0.33 -104 -100.2 44.8 0.33 -109 -114.4 205.4 3.4 76 0.221 SW 121.7 0.038 -177.2 0.33 -93.1 -95.5 104 0.33 -105 -101.7 59.7 0.33 -111 -115.9 242 2.7 77 0.193 SW 114.5 0.039 -176.8 0.33 -94.1 -96.7 71.9 0.33 -106 -102.7 30.1 0.33 -111 -116.5 147.5 2.9 78 0.223 SW 118.6 0.039 -176.9 0.33 -95.4 -98.1 79.3 0.33 -107 -104.1 53.2 0.33 -113 -118 249.7 3.5 79 0.205 SW 119.6 0.04 -176.9 0.33 -96.5 -99.2 65.1 0.33 -109 -105.5 59.4 0.33 -114 -119.4 240.5 6.7 80 0.222 SW 122 0.04 -176.9 0.33 -98.2 -100.8 101 0.33 -110 -106.9 68.8 0.33 -115 -120.7 230.6 3.1 81 0.203 SW 111.3 0.042 -177.7 0.33 -99.3 -102.1 78.3 0.33 -111 -108.2 45.8 0.33 -116 -121.9 219.1 2.6 82 0.22 SW 117.3 0.041 -177 0.33 -100 -103.1 58 0.33 -112 -109.3 44.4 0.33 -117 -122.6 180.9 3.2 83 0.197 SW 112.9 0.042 -177 0.33 -101 -104 51.6 0.33 -113 -110.4 43.9 0.33 -118 -123.7 235.1 3.2 84 0.174 SW 134.4 0.04 -176.4 0.33 -103 -105.5 105 0.33 -114 -111.5 47.6 0.33 -119 -125 246.3 2.6 85 0.198 SW 112.6 0.044 -176.9 0.33 -103 -106.4 43.2 0.33 -115 -112.5 26.5 0.33 -120 -125.7 185.5 3.1 86 0.207 SW 129.5 0.041 -176.4 0.33 -105 -107.8 100 0.33 -117 -114.1 99.6 0.33 -122 -127.2 274.1 1.9 87 0.222 SW 122.1 0.043 -177.6 0.33 -106 -109 81.7 0.33 -118 -115 19.9 0.33 -122 -128.1 214 7.5 88 0.243 SW 116.5 0.043 -176.3 0.33 -107 -110 60.6 0.33 -118 -115.8 25.1 0.33 -123 -128.7 178.6 4.1 89 0.138 SW 130.7 0.042 -176.8 0.33 -108 -111.1 72 0.33 -120 -117 67.7 0.33 -124 -129.8 252.2 2.4 90 0.226 SW 114.1 0.043 -176.4 0.33 -109 -112.3 88 0.33 -121 -118.3 63.6 0.33 -125 -130.8 242.1 3.6 91 0.172 SW 110.5 0.044 -176.4 0.33 -110 -113.5 81.9 0.33 -122 -119.6 80.8 0.33 -126 -131.7 221.7 3.1 92 0.224 SW 110.7 0.044 -176.9 0.33 -112 -114.9 109 0.33 -122 -120.5 40.2 0.33 -126 -132.3 179.5 4.0 93 0.276 SW 98.5 0.047 -177.1 0.33 -113 -116 70.6 0.33 -123 -121.5 61.7 0.33 -126 -132.7 171.9 1.9 94 0.184 SW 106.8 0.044 -177.1 0.33 -113 -116.9 71 0.33 -124 -122.5 49.9 0.33 -127 -133.6 227.1 3.2 95 0.183 SW 105.6 0.045 -177.1 0.33 -115 -118.2 101 0.33 -126 -123.7 84.7 0.33 -129 -134.7 240.3 3.0 96 0.183 SW 110.6 0.046 -178.2 0.33 -115 -118.9 37.2 0.33 -126 -124.2 3.8 0.33 -129 -135.5 213.7 6.0 97 0.26 SW 113.9 0.045 -177.6 0.33 -116 -120 91.9 0.33 -127 -125.3 57.5 0.33 -131 -136.7 270.8 3.6 98 0.179 SW 110.6 0.047 -177.8 0.33 -117 -120.9 68.2 0.33 -127 -125.8 1.23 0.33 -131 -137.2 185.3 3.3 99 0.18 SW 113.7 0.046 -177.5 0.33 -117 -121.2 14.1 0.33 -128 -126.1 26.3 0.33 -131 -137.4 151.7 4.7 100 0.176 SW 129.2 0.046 -177.9 0.33 -119 -123 161 0.33 -130 -127.9 99.1 0.33 -134 -139.6 417.9 6.0 101 0.218 SW 107 0.05 -178 0.33 -119 -123.5 28.3 0.33 -130 -128 15.9 0.33 -133 -139.7 132.2 3.6 102 0.129 SW 121.5 0.047 -177.5 0.33 -120 -123.9 27.6 0.33 -131 -129 23.9 0.33 -135 -141 318.9 3.2 103 0.166 SW 131 0.049 -178.2 0.33 -122 -125.4 137 0.33 -133 -130.7 106 0.33 -136 -142.4 320.4 2.2 104 0.202 SW 120.4 0.05 -178.3 0.33 -122 -126.3 75.9 0.33 -133 -130.9 20.7 0.33 -136 -142.3 151.8 2.5 105 0.149 SW 114.4 0.052 -178 0.33 -122 -126.6 2.77 0.33 -133 -131.2 13.3 0.33 -136 -143.1 219.5 3.4 106 0.12 SW 129.3 0.052 -178.7 0.33 -123 -127.6 94 0.33 -134 -132.5 5.15 0.33 -138 -144.2 317.4 1.9 107 0.208
167
EXP 19 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δ t ∆P SW 115.4 0.054 -178.6 0.33 -124 -128.1 37.9 0.33 -135 -132.9 20.1 0.33 -138 -144.6 198.3 2.1 108 0.184 SW 117.2 0.055 -178.5 0.33 -125 -129.5 138 0.33 -136 -134.3 68 0.33 -140 -146 365.8 3.3 109 0.191 SW 126.2 0.057 -178.9 0.33 -126 -130.3 73.4 0.33 -136 -134.8 17.9 0.33 -139 -146.1 148.2 3.3 110 0.238 SW 129 0.059 -178.6 0.33 -126 -130.3 12.4 0.33 -137 -135.1 1.72 0.33 -140 -146.5 227.7 4.0 111 0.247 SW 114.6 0.06 -178.8 0.33 -127 -131.7 121 0.33 -137 -136.1 31.6 0.33 -140 -146.9 210.3 1.9 112 0.146 SW 112.1 0.075 -178.2 0.33 -128 -131.3 19 0.33 -138 -136 15.1 0.33 -140 -146.9 214.4 3.1 113 0.106 SW 118 0.043 -178.5 0.33 -130 -134.2 248 0.33 -141 -139.5 363 0.33 -144 -150 661.7 4.3 114 0.145 SW 115.7 0.02 -178.4 0.42 -130 -133.6 5.34 0.42 -143 -139.5 106 0.17 -158 -163 3224 2.0 115 0.125 SW 106 0.061 -178.9 0.42 -133 -135.5 65.4 0.42 -157 -148 903 0.17 -168 -172.5 4065 3.9 116 0.137 SW 106 0.061 -178.7 -135.7 -155.2 -172.7 5.1 117 0.193 SW 117.3 0.063 -178.5 -137.4 -162.6 -173.2 4.0 118 0.145 SW 126.7 0.066 -178.9 -139.6 -166.8 -173.2 3.5 119 0.195 SW 116.9 0.065 -178.8 -142.4 -167.5 -173.2 4.7 120 0.135 SW 112.6 0.065 -178.6 -145 -169.9 -173.6 2.5 121 0.146 SW 126.2 0.071 -178.7 -148.1 -171 -173.4 3.4 122 0.172 SW 125.1 0.068 -179 -151.2 -172.5 -173.9 2.8 123 0.2 SW 126.9 0.074 -178.7 -156.4 -175.8 -175.5 2.3 124 0.241 SW 135.9 0.081 -179.2 -159.7 -176.5 -175.8 5.5 125 0.235 SW 126.3 0.081 -179.7 -160.5 -174.6 -174.1 2.0 126 0.141 SW 123.1 0.085 -179.6 -167.5 -176.6 -175.2 2.2 127 0.169 SW 126.6 0.084 -179.5 -169.9 -175.6 -175.1 4.7 128 0.238 SW 133.1 0.087 -180.3 -177.4 -178.6 -174.8 1.9 129 0.268 SW 119.3 0.089 -179.8 -178.1 -179 -176.8 4.1 130 0.206 SW 127.4 0.089 -179.8 -178.2 -177.1 -174.7 4.0 131 0.255 SW 127.5 0.089 -180.8 -179.1 -177.8 -176.2 3.1 132 0.211 SW 111.2 0.091 -180 -176.9 -176.5 -176.4 2.7 133 0.131 SW 120.7 0.089 -180.2 -178.8 -177.3 -176 3.3 134 0.189
EXP 20 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P N 120.2 1 7.2 0.33 22.9 23.7 609 0.33 23.8 24.5 258 0.33 23.2 24.7 246 0.0 0.0 1 0.151 N 123.6 1 2.8 0.33 19.7 20.9 862 0.33 20.3 21.6 910 0.33 20.1 22.2 760.4 0.0 0.0 2 0.261 N 129.8 1 -1 0.33 19 19.5 371 0.33 19.7 20.4 278 0.33 19.4 20.8 318.7 0.0 0.0 3 0.2 N 130 1 -4.6 0.33 17.5 18.1 390 0.33 17.6 18.7 388 0.33 16.9 18.6 582.2 0.0 0.0 4 0.226 N 129.4 1 -8.4 0.33 15.9 16.3 452 0.33 16.8 17.6 223 0.33 16.1 17.4 261.5 0.0 0.0 5 0.273 N 132.1 1 -11.8 0.33 14.1 14.5 423 0.33 15 15.8 362 0.33 14.6 15.9 330.7 0.0 0.0 6 0.272
168
EXP 20 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P N 133.1 1 -15.9 0.33 11.6 12.1 526 0.33 12 13.3 484 0.33 11.3 12.9 623.4 0.0 0.0 7 0.268 N 133.5 1 -20.1 0.33 9 9.4 559 0.33 10.1 11 406 0.33 9.8 11 346.3 0.0 0.0 8 0.265 N 132.4 1 -24.9 0.33 7.1 7.3 387 0.33 7.8 8.7 363 0.33 7.4 8.7 407.4 0.0 0.0 9 0.283 N 136.9 1 -30.9 0.33 4.5 4.6 453 0.33 5.6 6.6 290 0.33 5.1 6.3 372.7 0.0 0.0 10 0.413 N 137 1 -37.8 0.33 0.1 0.6 680 0.33 1 2.6 597 0.33 0.6 2.2 663.9 0.0 0.0 11 0.411 N 137.9 1 -40.4 0.33 -1.9 -2.1 391 0.33 -0.8 0.2 269 0.33 -1.2 -0.4 338.5 0.0 0.0 12 0.377 N 140.5 1 -49 0.33 -6.6 -6.4 477 0.33 -5.4 -4 396 0.33 -5.4 -4.2 401.3 0.0 0.0 13 0.425 N 142.4 1 -71.2 0.33 -10.9 -10.9 422 0.33 -9.4 -8.4 378 0.33 -8.7 -7.8 311.9 0.0 0.0 14 0.416 N 141.8 1 -83.1 0.33 -14.8 -15.1 350 0.33 -13.3 -12.2 262 0.33 -13.2 -12.2 351.1 0.0 0.0 15 0.433 N 143.2 1 -98.6 0.33 -20.7 -20.7 427 0.33 -19.2 -17.8 386 0.33 -18.6 -17.4 371.7 0.0 0.0 16 0.419 N 143.9 1 -111.6 0.33 -24 -24.7 297 0.33 -23.3 -22 267 0.33 -23.1 -22.4 350.3 0.0 0.0 17 0.4 N 143.5 1 -114.6 0.33 -29.1 -29.7 383 0.33 -28.3 -26.9 329 0.33 -27.9 -27.4 363.1 0.0 0.0 18 0.39 N 145.2 1 -117.8 0.33 -33.9 -34.6 338 0.33 -33.4 -32 310 0.33 -32.9 -32.6 336.6 0.0 0.0 19 0.377 N 146.4 1 -132.5 0.33 -38.5 -39.3 230 0.33 -38.6 -37.1 225 0.33 -38.2 -38 259.8 0.0 0.0 20 0.39 N 151.5 1 -176.2 0.33 -43.2 -44.1 237 0.33 -43.7 -42.4 240 0.33 -43 -43.2 248.3 0.0 0.0 21 0.418 N 157 1 -176.4 0.33 -49 -49.7 293 0.33 -50.2 -48.3 279 0.33 -50 -49.9 345.4 0.0 0.0 22 0.433 N 159.4 1 -176.7 0.33 -57.1 -57.4 408 0.33 -58.4 -56.1 388 0.33 -57.7 -57.6 407.9 0.0 0.0 23 0.42 N 160.1 1 -177.2 0.33 -62.2 -63.2 309 0.33 -63.8 -62.2 304 0.33 -63.1 -63.9 332.5 0.0 0.0 24 0.43 A 162.4 0.038 -177.4 0.33 -66 -67.7 244 0.33 -68.8 -67.2 252 0.33 -68.7 -69.9 345.9 0.0 2.5 25 0.424 A 159.9 1 -177.3 0.33 -71.3 -72.8 301 0.33 -74.3 -72.7 301 0.33 -74 -75.6 339.5 0.0 2.0 26 0.432 A 159.4 1 -177.3 0.33 -75.5 -77.4 271 0.33 -78.5 -77.5 264 0.33 -77.7 -79.9 269 0.0 1.8 27 0.432 A 156.7 0.032 -177.9 0.33 -80.6 -82.5 318 0.33 -83.4 -82.5 298 0.33 -82.3 -84.6 307.4 0.0 1.8 28 0.429 A 159.1 0.032 -177.6 0.33 -83.8 -86.2 235 0.33 -87.1 -86.4 230 0.33 -86.3 -89 296 0.0 1.8 29 0.427 N 159.9 1 -177.9 0.33 -89.4 -91.6 367 0.33 -92.1 -91.3 313 0.33 -90.9 -93.6 330.6 0.0 0.0 30 0.433 A 161.2 0.04 -177.7 0.33 -92.6 -95.4 251 0.33 -95.8 -95.6 280 0.33 -94.2 -97.5 273.9 0.6 2.2 31 0.43 A 163.1 0.04 -178.6 0.33 -97.8 -100.3 360 0.33 -101.2 -100.5 342 0.33 -99.7 -102.7 402.8 0.4 2.4 32 0.43 A 164.4 0.04 -178.5 0.33 -99.6 -102.9 181 0.33 -103.4 -103.6 212 0.33 -101.7 -105.7 226.9 0.3 2.9 33 0.433 A 166.2 0.039 -178.3 0.33 -103.5 -106.8 314 0.33 -106.5 -106.6 213 0.33 -104.9 -108.9 275.3 0.4 2.1 34 0.426 A 169.8 0.04 -178.4 0.33 -106.6 -110 254 0.33 -110 -110.3 290 0.33 -107.9 -112.1 276.4 0.6 4.0 35 0.42 A 178.4 0.041 -178.4 0.33 -112.4 -115.2 441 0.33 -115.6 -115.8 474 0.33 -112.4 -116.3 375.3 0.3 2.5 36 0.4 A 184.4 0.042 -178.9 0.33 -112.4 -116.6 98 0.33 -117.3 -117.6 123 0.33 -116 -120.3 381.5 0.4 3.7 37 0.381 A 190.6 0.042 -177.8 0.33 -115.8 -119.6 280 0.33 -119.9 -120.4 254 0.33 -117.8 -122.7 229.5 0.4 2.9 38 0.405 A 195.8 0.043 -178.6 0.33 -117.7 -121.8 204 0.33 -121.8 -122.7 207 0.33 -119.5 -124.7 211.2 0.5 2.9 39 0.377 A 198.3 0.043 -179 0.33 -122.1 -126 419 0.33 -124.7 -126 333 0.33 -121.2 -126.5 195.1 0.3 1.8 40 0.38 A 201.6 0.043 -178.8 0.33 -124.7 -129 300 0.33 -128.1 -129.1 314 0.33 -124.9 -129.9 378.3 0.4 2.3 41 0.39 A 206.3 0.044 -179 0.33 -125.5 -130.2 118 0.33 -129.8 -131.2 220 0.33 -126.8 -132.2 256.1 0.4 2.2 42 0.38 A 211.1 0.044 -179.5 0.33 -127 -131.9 200 0.33 -130.3 -132.1 102 0.33 -127.2 -133.1 114.5 0.3 2.2 43 0.378 A 218.5 0.045 -178.9 0.33 -130.9 -134.9 356 0.33 -135.4 -136.2 493 0.33 -132.1 -137.1 500.6 0.4 3.0 44 0.391 A 217.5 0.045 -179.4 0.33 -132.4 -137.1 256 0.33 -136.8 -138 197 0.33 -134.2 -139.8 341.9 0.3 1.8 45 0.395 A 219.5 0.044 -179.1 0.33 -133.1 -137.9 77.3 0.33 -137.8 -140 298 0.33 -133.5 -140 13.94 0.4 1.4 46 0.376
169
EXP 20 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P A 223.7 0.045 -179.4 0.33 -133.3 -138.2 42.7 0.33 -139.8 -140.7 95.8 0.33 -137.8 -143.4 497.4 0.3 2.0 47 0.375 A 229.9 0.046 -179.9 0.33 -135.6 -140.6 313 0.33 -139.6 -141.3 50.5 0.33 -137.1 -142.7 54.6 0.4 1.6 48 0.35 A 232.4 0.045 -179.7 0.33 -137.9 -142.8 294 0.33 -141.9 -143.5 320 0.33 -138.6 -143.9 214 0.3 2.1 49 0.344 A 239 0.046 -180.2 0.33 -138.1 -142.5 90.1 0.33 -142.1 -143.3 126 0.33 -138.4 -145.1 52.5 0.4 2.4 50 0.345 A 239.2 0.046 -180.4 0.33 -140.5 -145.9 354 0.33 -143.1 -145.5 181 0.33 -139 -145.6 103.3 0.4 2.0 51 0.371 A 243.7 0.047 -180.2 0.33 -142.7 -148.2 366 0.33 -145.3 -147.4 302 0.33 -141 -147.3 286.7 0.4 2.7 52 0.358 A 247.9 0.047 -179.7 0.33 -143.5 -149 129 0.33 -147.8 -149.8 414 0.33 -143.6 -149.7 396.9 0.4 3.7 53 0.366 A 247.6 0.046 -180 0.33 -144.8 -150.3 231 0.33 -148.7 -151 189 0.33 -144.7 -151.3 263.2 0.4 2.7 54 0.374 A 243.3 0.046 -180.5 0.33 -148.2 -152 271 0.33 -165.1 -161.9 2415 0.33 -166.7 -169.4 3519 0.1 5.1 55 0.37 A 254.3 0.049 -180.4 -152.1 -171.6 -170.8 0.1 3.3 56 0.362 A 265.8 0.054 -180.3 -154.3 -176.9 -175.8 0.2 2.7 57 0.361 A 270.7 0.058 -181.1 -160.3 -178.7 -178.4 0.4 2.1 58 0.356 A 279 0.061 -181.5 -165.2 -178.7 -178.5 0.4 3.4 59 0.319 A 271.7 0.063 -181.2 -172.2 -174.3 -172 0.2 1.6 60 0.346 A 265.3 0.065 -181 -176 -176 -174.4 0.3 2.6 61 0.323 A 264.8 0.065 -181.6 -176.7 -178.7 -178.4 0.3 2.4 62 0.329 A 255.9 0.064 -181.3 -178.5 -177.6 -175.7 0.5 3.7 63 0.302 A 246.8 0.064 -182 -181.4 -182.8 -180.3 0.6 3.3 64 0.328 A 246.8 0.064 -181.6 -177.8 -177.7 -176.6 0.4 3.0 65 0.304 A 240.1 0.064 -181.8 -175.3 -176.6 -175.2 0.2 1.9 66 0.312 A 236.7 0.064 -182.4 -183.9 -183.4 -179.5 0.4 3.3 67 0.306 EXP 21 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P N 150 1 7.4 0.33 21.1 23.8 473.2 0.33 21.6 23.8 486 0.33 21.9 24.2 328 0.0 0.0 1 0.27 N 146.2 1 0.2 0.33 19.6 21.7 489.9 0.33 19.8 22.2 343 0.33 20.1 22.6 374.8 0.0 0.0 2 0.187 N 150.7 1 -8.2 0.33 17.3 19.2 474.5 0.33 17.3 19.8 449 0.33 17.3 20.1 467.7 0.0 0.0 3 0.275 N 155.5 1 -17 0.33 13.8 16 291.9 0.33 14.3 16.8 262 0.33 14.4 16.9 282.1 0.0 0.0 4 0.231 N 164.8 1 -62.5 0.33 9 10.3 452.1 0.33 9.3 11.3 420 0.33 9.8 11.6 406.5 0.0 0.0 5 0.291 N 172.1 1 -79.7 0.33 4 3.9 421.1 0.33 4.3 4.7 432 0.33 4.7 5.1 427.8 0.0 0.0 6 0.4 N 179.2 1 -99.5 0.33 -3.6 -4.2 604.1 0.33 -3.8 -3.3 572 0.33 -2.8 -3.4 620.2 0.0 0.0 7 0.333 N 171.4 1 -94.3 0.33 -10.6 -11.4 538.2 0.33 -10.2 -10.1 477 0.33 -9.7 -10.3 503.2 0.0 0.0 8 0.357 S 174.6 1 -99.1 0.33 -17.7 -18.9 569 0.33 -17.6 -17.5 541 0.33 -17.3 -17.6 541.2 0.0 1.8 9 0.336 N 173.9 1 -104.5 0.33 -25.2 -25.6 489.9 0.33 -25.7 -23.9 437 0.33 -24.5 -24.3 480 0.0 0.0 10 0.333 N 173.9 1 -114.6 0.33 -32.3 -32.5 325.7 0.33 -33 -31 319 0.33 -33.3 -31.4 329.1 0.0 0.0 11 0.402 A 203.5 1 -171.1 0.33 -39.5 -40.1 372.2 0.33 -40.5 -39.2 389 0.33 -40.6 -39.7 401.9 0.6 2.2 12 0.334 A 190.2 1 -173.1 0.33 -46.8 -48.3 416.4 0.33 -48.1 -47 370 0.33 -48.5 -48 418.3 0.4 2.4 13 0.365 A 213.3 0.044 -172.9 0.33 -54.8 -56 406.6 0.33 -56.7 -55.4 428 0.33 -57.2 -57.1 486 0.3 2.9 14 0.409
170
EXP 21 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P A 210.5 0.043 -172.5 0.33 -62.4 -63.5 418.5 0.33 -64.9 -63.3 419 0.33 -65.6 -65.3 464.4 0.4 2.1 15 0.36 A 216.4 0.044 -173 0.33 -69.4 -70.7 418.9 0.33 -72.2 -70.9 431 0.33 -73 -73.6 497.4 0.6 4.0 16 0.374 A 218.1 0.045 -172.6 0.33 -75.7 -77.5 416.4 0.33 -78.6 -77.8 406 0.33 -79.8 -80.5 436.4 0.3 2.5 17 0.387 A 224.2 0.046 -172.9 0.33 -81.3 -84.2 431.4 0.33 -84.5 -84.9 455 0.33 -85.3 -87.5 482.1 0.4 3.7 18 0.424 A 228.7 0.047 -172.5 0.33 -86.2 -90.5 434.2 0.33 -89.7 -91.3 418 0.33 -91 -94 468.6 0.4 2.9 19 0.429 A 220.7 0.046 -173 0.33 -91.7 -96.4 414.7 0.33 -95.1 -97.3 423 0.33 -96.2 -99.6 431.5 0.5 2.9 20 0.399 A 219.2 0.045 -174.1 0.33 -96.3 -101.9 412.1 0.33 -100.3 -103 434 0.33 -100.7 -105.1 440.2 0.3 1.8 21 0.402 A 235.2 0.049 -173.9 0.33 -100.6 -106.5 359.7 0.33 -104.5 -107.7 373 0.33 -105.6 -109.8 405.3 0.4 2.3 22 0.363 A 243 0.051 -174.4 0.33 -107.7 -110.5 337.3 0.33 -112.4 -112 367 0.33 -112.4 -113.7 351.5 0.4 2.2 23 0.369 A 260.1 0.055 -174.1 0.33 -110.6 -116 492.1 0.33 -114.7 -117.5 509 0.33 -114.4 -119.1 525.2 0.3 2.2 24 0.402 A 255.4 0.054 -174.5 0.33 -114 -119.7 335.9 0.33 -119.9 -121.2 344 0.33 -120.5 -123.1 401.9 0.4 3.0 25 0.357 A 267.1 0.057 -174.7 0.33 -116.7 -123.5 364.7 0.33 -121.9 -124.9 380 0.33 -122.2 -126.2 342.4 0.3 1.8 26 0.393 A 269.2 0.058 -175.3 0.33 -120 -126.4 290.5 0.33 -125.6 -127.6 284 0.33 -125.2 -129.3 352.6 0.4 1.4 27 0.359 A 279.2 0.061 -175.8 0.33 -122.7 -129.5 340.4 0.33 -128.4 -130.9 388 0.33 -128.6 -132.5 393.6 0.3 2.0 28 0.353 A 284.9 0.062 -175.4 0.33 -125.2 -131.6 227.1 0.33 -131 -132.8 218 0.33 -130.9 -134.2 204 0.4 1.6 29 0.352 A 298.7 0.067 -176.6 0.33 -127.4 -134.2 326.4 0.33 -134.1 -135.6 367 0.33 -133.9 -136.6 339.1 0.3 2.1 30 0.345 A 315.3 0.072 -176 0.33 -128.9 -136 210.1 0.33 -134.6 -137.4 230 0.33 -134.8 -138.4 247.4 0.4 2.4 31 0.343 A 335.6 0.079 -177 0.33 -130.8 -138.1 270 0.33 -134.8 -139.8 341 0.33 -134.7 -141.2 402.2 0.4 2.0 32 0.338 A 354.9 0.086 -177.2 0.33 -132.7 -140 241.9 0.33 -136.9 -141.3 203 0.33 -136.5 -142.3 163.3 0.4 2.7 33 0.337 A 356.8 0.088 -177.3 0.33 -134 -141.9 264.1 0.33 -139.4 -143.4 322 0.33 -139.8 -144.5 349.6 0.4 3.7 34 0.294 A 352.2 0.086 -178.3 0.33 -135.9 -142.4 55.9 0.33 -140.2 -144.2 140 0.33 -139.3 -145.5 177.1 0.4 2.7 35 0.276 A 349 0.085 -177.4 0.33 -137.3 -145.2 433.9 0.33 -142.7 -146.9 461 0.33 -141.6 -147.6 375.2 0.4 3.4 36 0.293 A 345.3 0.044 -177.7 0.33 -138.8 -146.6 124.4 0.33 -144.9 -157.8 2029 0.33 -143.9 -163 2808 0.1 4.7 37 0.295 A 344.2 0.044 -177.8 0.33 -139.5 -147.7 9.4 0.33 -145.6 -168.9 3913 0.33 -144.3 -169.3 2524 0.1 4.7 38 0.285 A 345.8 0.084 -178.1 -152.7 -173.5 -171.6 0.3 2.1 39 0.315 A 333.1 0.084 -177.9 -158.9 -172.5 -171.1 0.2 2.7 40 0.319 A 335.3 0.086 -179.2 -172.4 -174.8 -173 0.4 2.1 41 0.301 A 314.1 0.086 -179 -175.7 -174.2 -170.7 0.4 3.4 42 0.288 A 318.2 0.087 -178.7 -176.8 -176.2 -173.3 0.2 1.6 43 0.298 A 319.4 0.086 -179.1 -178.9 -176.6 -172.2 0.3 2.6 44 0.336 A 303.1 0.086 -179.5 -174.3 -174.1 -172.7 0.3 2.4 45 0.267 A 318.4 0.086 -179.6 -175.8 -173 -168.5 0.5 3.7 46 0.274 A 291.8 0.087 -180.1 -175.9 -175.3 -174.1 0.6 3.3 47 0.213 A 304.4 0.086 -180.6 -178.9 -175.2 -171.6 0.4 3.0 48 0.28 A 284.8 0.088 -179.8 -177.6 -179.3 -178 0.2 1.9 49 0.235 A 278.8 0.088 -180.3 -175.5 -172.3 -167.6 0.4 3.3 50 0.292 A 282.3 0.087 -180.2 -177.2 -177.2 -176 0.3 2.3 51 0.24 A 260.6 0.089 -181.2 -179.4 -178.4 -174.8 0.4 3.0 52 0.272 A 292.4 0.086 -181.4 -176.7 -174.5 -172.7 0.4 2.0 53 0.256
171
EXP 22 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P N 104.1 1 1.9 0.33 20.1 21.5 668 0.33 20.8 22.2 491 0.33 21.1 22.5 439 0.0 0.0 1 0.211 N 126.1 1 -10.3 0.33 17.6 18.8 396 0.33 18.2 19.6 355 0.33 18.1 19.6 421 0.0 0.0 2 0.217 N 140.5 1 -28.3 0.33 11.3 13.2 542 0.33 12.5 14.7 447 0.33 12.8 14.9 434 0.0 0.0 3 0.243 N 152.8 1 -60.6 0.33 2.8 5.2 611 0.33 3.5 6.7 594 0.33 4.2 7.3 567 0.0 0.0 4 0.373 N 170.3 1 -85.2 0.33 -7.9 -5.1 726 0.33 -8.1 -4.2 755 0.33 -7.9 -3.8 772 0.0 0.0 5 0.352 N 169.8 1 -99.1 0.33 -18.7 -16.3 549 0.33 -17.8 -14.3 470 0.33 -17.6 -14.1 488 0.0 0.0 6 0.296 N 175.4 1 -151.3 0.33 -29 -27.1 506 0.33 -29.6 -25.9 538 0.33 -29.2 -25.5 528 0.0 0.0 7 0.314 N 181.9 3.139 -164.9 0.33 -40.8 -39.1 600 0.33 -41 -37.5 553 0.33 -41.4 -37.9 609 0.0 0.0 8 0.34 A 173.3 0.074 -165.9 0.33 -48.6 -48.4 465 0.33 -49.2 -46.9 446 0.33 -50 -47.7 487 0.2 2.8 9 0.34 A 198.8 0.076 -170.1 0.33 -58.5 -58.4 553 0.33 -60.1 -57.6 580 0.33 -60.6 -58.2 575 0.2 2.7 10 0.322 A 236.3 0.065 -168.9 0.33 -67.9 -68.1 567 0.33 -70.6 -68.3 616 0.33 -71.7 -69.4 658 0.1 3.0 11 0.314 A 225.8 0.103 -170 0.33 -76.6 -77.5 577 0.33 -79.6 -77.9 585 0.33 -81 -79.4 629 0.2 2.4 12 0.356 A 214.1 0.083 -170.4 0.33 -84.8 -86.2 578 0.33 -88.4 -87.2 612 0.33 -89.6 -88.6 623 0.2 2.7 13 0.36 A 211.7 0.05 -170.8 0.33 -91.7 -93.8 535 0.33 -95.8 -95.1 573 0.33 -96.8 -96.4 577 0.2 3.3 14 0.356 A 234.4 0.046 -170.8 0.33 -98.3 -100.9 536 0.33 -102.5 -102.3 556 0.33 -103.3 -103.4 550 0.8 1.2 15 0.362 A 252.6 0.067 -171.7 0.33 -103.8 -107 490 0.33 -108.5 -108.8 549 0.33 -109.5 -109.9 564 0.2 2.5 16 0.322 A 270.2 0.037 -171.5 0.33 -109.1 -112.8 498 0.33 -113.8 -114.4 519 0.33 -114.5 -115.4 502 0.3 3.7 17 0.327 A 292.6 0.096 -171.9 0.33 -113.8 -117.9 483 0.33 -118.1 -119.2 449 0.33 -119.6 -120.7 539 0.3 1.5 18 0.312 A 299 0.074 -172 0.33 -118.3 -122.8 488 0.33 -122.4 -123.7 451 0.33 -123.9 -125.4 504 0.1 2.6 19 0.335 A 276.7 0.108 -173.1 0.33 -122.6 -127.4 497 0.33 -127.1 -128.4 524 0.33 -128.2 -129.9 523 0.2 1.7 20 0.338 A 254.2 0.11 -173.3 0.33 -125.6 -131 394 0.33 -130.4 -132.2 449 0.33 -131.1 -133.2 412 0.3 1.5 21 0.344 A 251.4 0.069 -174.1 0.33 -129 -134.5 441 0.33 -133.7 -135.6 449 0.33 -134.3 -136.5 441 0.3 2.6 22 0.331 A 279.2 0.065 -174 0.33 -131.4 -137.3 356 0.33 -136.3 -138.6 417 0.33 -136.9 -139.2 398 0.3 2.5 23 0.32 A 318.5 0.165 -174 0.33 -133.7 -139.9 371 0.33 -137.7 -140.3 249 0.33 -138 -140.8 241 0.2 1.1 24 0.318 A 337 0.051 -174.4 0.33 -135.8 -142.2 349 0.33 -139.5 -142.2 325 0.33 -138.3 -141.3 71 0.2 3.4 25 0.296 A 357.2 0.061 -174.6 0.33 -137.6 -144.4 371 0.33 -139.9 -142.8 63 0.33 -140.2 -143 307 0.3 2.9 26 0.328 A 398.7 0.096 -174.7 0.33 -139.9 -146.3 308 0.33 -146.6 -148.4 1005 0.33 -146.6 -148.1 860 0.3 1.8 27 0.33 A 471 0.106 -175 0.33 -140.8 -147.7 256 0.33 -146.2 -149.3 115 0.33 -147.8 -150.7 469 0.2 1.9 28 0.32 A 397.4 0.081 -175.1 0.33 -144.9 -149.8 320 0.33 -161.8 -161.8 2788 0.33 -167.6 -166.7 3566 0.3 1.6 29 0.354 A 501.7 0.129 -175.6 0.33 -147.3 -151.5 125 0.33 -167.5 -169.8 4993 0.33 -166.2 -169.1 1492 0.3 2.6 30 0.323 A 582.5 0.104 -175.4 -155.7 -184.5 -178.9 0.3 2.1 31 0.349 A 599.5 0.061 -176.4 -161.1 -172.7 -171 0.3 2.9 32 0.349 A 599.8 0.057 -176.2 -169.2 -177.9 -174.3 0.2 3.0 33 0.306 A 569.4 0.082 -176.9 -173.8 -171.8 -172.5 0.2 2.9 34 0.318 A 602.6 0.043 -176.8 -174.8 -179.3 -174.8 0.3 3.8 35 0.29 A 588.4 0.122 -177.7 -175.6 -174.5 -175.6 0.3 4.4 36 0.279 A 606.3 0.071 -178.5 -176.9 -169.4 -171.2 0.3 3.5 37 0.245 A 571.9 0.069 -178.4 -177 -168.2 -166.8 0.2 3.7 38 0.273 A 536.6 0.167 -177.9 -177.1 -177 -173.6 0.2 3.4 39 0.284 A 531.5 0.06 -178.9 -177.7 -169.7 -170 0.2 4.2 40 0.289
172
EXP 22 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P A 560.8 0.106 -179.4 -178.4 -177.4 -169.3 0.2 4.8 41 0.252 A 486.7 0.105 -179.3 -178.8 -175.4 -169.4 0.3 4.6 42 0.245 EXP 23 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P N 159.6 1 4.8 0.33 21.1 22.2 595 0.33 21.6 22.8 409 0.33 21.9 23 353 0.0 0.0 1 0.138 N 163.8 1 -2.5 0.33 19.6 20.5 381 0.33 19.8 20.9 418 0.33 20.1 21.3 394 0.0 0.0 2 0.268 N 169 1 -9.6 0.33 17.3 18.4 398 0.33 17.3 18.6 409 0.33 17.3 18.7 463 0.0 0.0 3 0.207 N 176 1 -20.1 0.33 13.8 15.1 454 0.33 14.3 15.8 368 0.33 14.4 15.8 376 0.0 0.0 4 0.3 N 182.1 1 -36.4 0.33 9 10.5 525 0.33 9.3 11.2 524 0.33 9.8 11.7 470 0.0 0.0 5 0.293 N 184.1 1 -49.1 0.33 4 5.4 435 0.33 4.3 6.4 398 0.33 4.7 6.7 413 0.0 0.0 6 0.333 N 193.3 1 -75.5 0.33 -3.6 -1.8 562 0.33 -3.8 -1.1 579 0.33 -2.8 -0.1 520 0.0 0.0 7 0.354 N 192.5 1 -88.6 0.33 -10.6 -9.1 541 0.33 -10.2 -7.8 476 0.33 -9.7 -7.2 509 0.0 0.0 8 0.312 N 194.1 1 -98.9 0.33 -17.7 -16.5 372 0.33 -17.6 -15.2 355 0.33 -17.3 -14.8 373 0.0 0.0 9 0.35 N 200.9 1 -149.6 0.33 -25.2 -24.3 418 0.33 -25.7 -23.3 438 0.33 -24.5 -22.1 382 0.0 0.0 10 0.349 N 202.8 0.076 -145.3 0.33 -32.3 -31.8 365 0.33 -33 -30.8 352 0.33 -33.3 -30.8 419 0.0 2.5 11 0.352 N 204.8 1 -165.8 0.33 -39.5 -39.3 368 0.33 -40.5 -38.5 369 0.33 -40.6 -38.7 375 0.0 0.0 12 0.368 N 210.8 1 -169.7 0.33 -46.8 -46.9 389 0.33 -48.1 -46.3 388 0.33 -48.5 -46.7 408 0.0 0.0 13 0.343 N 220 0.139 -169.8 0.33 -54.8 -55 440 0.33 -56.7 -54.8 456 0.33 -57.2 -55.4 469 0.0 1.8 14 0.385 N 227.9 1 -169.6 0.33 -62.4 -63.1 449 0.33 -64.9 -63.3 472 0.33 -65.6 -64 487 0.0 0.0 15 0.396 N 227.3 1 -170.5 0.33 -69.4 -70.5 439 0.33 -72.2 -71.1 456 0.33 -73 -71.9 472 0.0 0.0 16 0.393 A 223 0.043 -170.4 0.33 -75.7 -77.4 428 0.33 -78.6 -77.9 419 0.33 -79.8 -79.2 460 0.6 2.2 17 0.363 A 221.4 0.049 -171 0.33 -81.3 -83.6 396 0.33 -84.5 -84.2 410 0.33 -85.3 -85.2 402 0.4 2.4 18 0.379 A 218.5 0.043 -171.6 0.33 -86.2 -88.9 362 0.33 -89.7 -89.8 377 0.33 -91 -91.2 426 0.3 2.9 19 0.388 A 225.8 0.053 -172 0.33 -91.7 -94.6 413 0.33 -95.1 -95.3 399 0.33 -96.2 -96.7 407 0.4 2.1 20 0.395 A 228.4 0.023 -171.8 0.33 -96.3 -99.6 370 0.33 -100.3 -100.7 425 0.33 -100.7 -101.5 378 0.6 4.0 21 0.393 A 229.3 0.053 -172.1 0.33 -100.6 -104.3 367 0.33 -104.5 -105.3 359 0.33 -105.6 -106.5 416 0.3 2.5 22 0.371 A 234.6 0.031 -173.1 0.33 -107.7 -110.8 562 0.33 -112.4 -112.5 653 0.33 -112.4 -112.7 556 0.4 3.7 23 0.393 A 242.7 0.045 -173 0.33 -110.6 -115 351 0.33 -114.7 -116.2 331 0.33 -114.4 -116 282 0.4 2.9 24 0.375 A 243 0.042 -173.6 0.33 -114 -118.4 312 0.33 -119.9 -121.1 515 0.33 -120.5 -121.4 545 0.5 2.9 25 0.384 A 241.9 0.088 -173.6 0.33 -116.7 -121.5 293 0.33 -121.9 -123.9 296 0.33 -122.2 -124.2 267 0.3 1.8 26 0.357 A 231.6 0.057 -174.3 0.33 -120 -124.8 331 0.33 -125.6 -127.4 426 0.33 -125.2 -127.1 320 0.4 2.3 27 0.387 A 238.2 0.057 -174.5 0.33 -122.7 -127.8 308 0.33 -128.4 -130.4 382 0.33 -128.6 -130.4 386 0.4 2.2 28 0.394 A 237.2 0.063 -174.7 0.33 -125.2 -130.6 294 0.33 -131 -133.2 375 0.33 -130.9 -133 308 0.3 2.2 29 0.376 A 253.1 0.045 -175.1 0.33 -127.4 -132.8 249 0.33 -134.1 -136.4 463 0.33 -133.9 -135.9 374 0.4 3.0 30 0.361 A 256.9 0.091 -175.1 0.33 -128.9 -134.7 214 0.33 -134.6 -137.5 174 0.33 -134.8 -137.5 196 0.3 1.8 31 0.373 A 258.8 0.086 -175.1 0.33 -130.8 -136.8 266 0.33 -134.8 -137.8 63 0.33 -134.7 -137.8 42 0.4 1.4 32 0.348 A 262.9 0.086 -176 0.33 -132.7 -138.9 266 0.33 -136.9 -139.6 279 0.33 -136.5 -139.1 212 0.3 2.0 33 0.346
173
EXP 23 Region 1 Region 2 Region 3
FR G x Tsat A1 Tw,i Tw,t h1 A2 Tw,i Tw,s h2 A3 Tw,i Tw,b h3 δt δb t ∆P A 266.5 0.085 -176.1 0.33 -134 -140.3 190 0.33 -139.4 -141.9 370 0.33 -139.8 -142.1 431 0.4 1.6 34 0.355 A 268.8 0.084 -176.6 0.33 -135.9 -142.3 288 0.33 -140.2 -143.2 220 0.33 -139.3 -142.4 22 0.3 2.1 35 0.364 A 279 0.065 -176.4 0.33 -137.3 -143.8 220 0.33 -142.7 -145.5 437 0.33 -141.6 -144.1 285 0.4 2.4 36 0.368 A 283.2 0.082 -176.4 0.33 -138.8 -145.2 213 0.33 -144.9 -147.7 463 0.33 -143.9 -146.2 343 0.4 2.0 37 0.344 A 286.6 0.063 -176.4 0.33 -139.5 -146.2 142 0.33 -145.6 -148.8 269 0.33 -144.3 -147.2 131 0.4 2.7 38 0.308 A 298.8 0.044 -176.9 0.33 -141.3 -147.5 201 0.33 -149.4 -152.1 756 0.33 -148.2 -150.2 535 0.4 3.7 39 0.319 A 380.8 0.053 -176.8 0.33 -142 -148.5 138 0.33 -150 -152.1 128 0.33 -155.3 -157.2 1417 0.4 2.7 40 0.338 A 351.7 0.039 -177 0.33 -144.8 -149.9 147 0.33 -161 -162.2 2268 0.33 -165.7 -166.7 2631 0.4 3.4 41 0.318 A 414.6 0.053 -177.2 0.33 -147.3 -151.3 64 0.33 -168.2 -170.5 4210 0.33 -166.5 -169.1 1150 0.3 2.1 42 0.357 A 457.9 0.073 -176.9 0.33 -152.8 0.33 -173.7 0.33 -172.6 0.2 2.7 43 0.353 A 465.4 0.081 -177.3 0.33 -156.4 0.33 -175 0.33 -172.4 0.4 2.1 44 0.34 A 472.6 0.048 -177.7 0.33 -160.8 0.33 -176.9 0.33 -174.6 0.4 3.4 45 0.344 A 510.2 0.132 -177.8 0.33 -166.1 0.33 -176.1 0.33 -173.3 0.2 1.6 46 0.328 A 475 0.075 -177.8 0.33 -171.6 0.33 -175.5 0.33 -173.6 0.3 2.6 47 0.323 A 487 0.085 -178.2 0.33 -174.6 0.33 -175.5 0.33 -172.3 0.3 2.4 48 0.332 A 485.8 0.038 -178.4 0.33 -175.4 0.33 -172.3 0.33 -170.2 0.5 3.7 49 0.338 A 422.8 0.043 -178.4 0.33 -175.8 0.33 -173.9 0.33 -171.1 0.6 3.3 50 0.324 A 449.5 0.059 -179 0.33 -176.3 0.33 -174 0.33 -171.5 0.4 3.0 51 0.317 A 440.7 0.117 -179.1 0.33 -176.5 0.33 -175.9 0.33 -172.8 0.2 1.9 52 0.337 A 417 0.049 -179.3 0.33 -176.8 0.33 -175.4 0.33 -172.8 0.4 3.3 53 0.293 A 415.3 0.088 -179.6 0.33 -177.2 0.33 -176.1 0.33 -173.2 0.3 2.3 54 0.292 A 425.3 0.06 -179.5 0.33 -177.4 0.33 -172.6 0.33 -171.8 0.4 3.0 55 0.314 A 404.7 0.09 -179.4 0.33 -176.8 0.33 -177.5 0.33 -176.2 0.4 2.0 56 0.289 A 461.3 0.054 -179.8 0.33 -177.6 0.33 -175.1 0.33 -171.4 0.4 2.9 57 0.283 A 403.1 0.058 -180.2 0.33 -177.9 0.33 -176.8 0.33 -173.4 0.3 3.2 58 0.327 A 332.1 0.054 -179.9 0.33 -177.8 0.33 -173.6 0.33 -173.6 0.4 3.3 59 0.315 A 355.1 0.061 -180 0.33 -178.5 0.33 -172.3 0.33 -171.6 0.3 3.3 60 0.248 A 362.1 0.08 -180.6 0.33 -178 0.33 -173.1 0.33 -174.9 0.4 2.4 61 0.287 A 387.5 0.053 -180.1 0.33 -178.6 0.33 -164.5 0.33 -166.7 0.3 3.5 62 0.312
174
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BIOGRAPHICAL SKETCH
Jelliffe Kevin Jackson was the second of four children born to Victor and Eva
Jackson on the southern most Caribbean island of Trinidad. He received his BSc in
mechanical engineering with First Class Honors from The University of the West Indies,
St. Augustine, Trinidad, in May of 2000. He received a Fulbright Fellowship which gave
him the opportunity to earn his MSc in aerospace engineering from the University of
Florida in May 2003. His is currently working toward his PhD in mechanical
engineering under the guidance of Professor James Klausner at the University of Florida.