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Scholars' Mine Scholars' Mine
Masters Theses Student Theses and Dissertations
1967
The relation of heat transfer to mass transfer in vaporization The relation of heat transfer to mass transfer in vaporization
through porous membranes. through porous membranes.
Chung-Liang Yeh
Follow this and additional works at: https://scholarsmine.mst.edu/masters_theses
Part of the Chemical Engineering Commons
Department: Department:
Recommended Citation Recommended Citation Yeh, Chung-Liang, "The relation of heat transfer to mass transfer in vaporization through porous membranes." (1967). Masters Theses. 5041. https://scholarsmine.mst.edu/masters_theses/5041
This thesis is brought to you by Scholars' Mine, a service of the Missouri S&T Library and Learning Resources. This work is protected by U. S. Copyright Law. Unauthorized use including reproduction for redistribution requires the permission of the copyright holder. For more information, please contact [email protected].
'rHE REIJ1.TION OF HEAT ·rRAlJSFER
TO J.1ASS TRANSFER IN VAPOB.IZATICN
rrHROUGH POROUS IviEr'IBRll..NES
BY
CHUNG-LIAJ:.JG YEH - I 1 ,:os i-
A
THESIS
submitted to the faculty of
'rHE UNIVERSITY OF NISSOURI A'r ROLLA
in partial fulfillment of the requirements for the
Degree of
NASTER OF SCIENCE IN CHENICAL ENGINEERING
.)
.~ 3 .·· /' ... ;.· '"
. ) l l
~~. )) -.~
Approved by
ii
ABSTRACT
·rhe object of this investigation was to study the mass
and heat transport phenomena through porous, water-repellent
membranes. The investigation concerned the rate of vaporiza
tion of salt water at a porous membrane surface, mass transfer
of vapor through the pores of the membrane, condensation of
vapor on the other surface of the membrane in contact with
a coolant (fresh water), and the undesired heat transfer by
conduction through the membrane.
The water-repellent membrane separated the two liquid
phases by surface tension forces and provided a vapor phase
in its pores. Membranes made of fiberglass and Teflon had
been found suitable for this study, and were used throughout
the investigation with several different thickness.
The temperature difference between the two liquid phases
maintained the driving force the corresponding vapor pres-
sure difference - for mass transfer. Also, it supplied the
driving force for the undesired heat transfer across the
membrane.
Theoretical and empirical correlations were proposed to
fit the experimental data. It was observed that diffusional
resistance is the major rate controlling factor for mass
transfer. The correlations developed predicted values of
mass transfer coefficient reasonably close to the experimental
values, but there were differences between the correlation
for heat transfer coefficient and the experimental values.
iii
It I·Jas observed that the mass transfer rate ranged from 0. 23 2 to 1.41 lb./ft. hr., vii th total heat transfer rates from
2 43.4 to 272 Btu./ft. hr •• The mass transfer coefficients
2 varied from 0.114 to 0.420 lb./ft. hr. in. Hg •• The heat
conducted through the membrane was used to calculate an over-
all heat transfer coefficients which varied from 5.6 to 21.9
I 2 0 Btu. ft. hr. F.
iv
ABSTR.l\c~r • • • • • • • • • • • • • • • • • • • • • • • LIST OF FIGURES. • • • • • • • • • • • • • • • • • • • LIST OF TABLES • • • • • • • • • • • • • • • • • • • • :tJ 0 IIEl.J C LA T URE • • • • • • • • • • • • • • • • • • • • •
PAGE ii vi vii viii
I. INTRODUCTION • • • • • • • • • • • • • • • • • 1
II. THEOREJIICAL ANALYSIS AND LITERATURE B.E.VIEt..r • • .3
A. r~Iembranes • • • • • • • • • • • • • • • • • .3 B. Theory of f•Iass Transfer • • • • • • . • • • 4
1. Equilibrium and 1'-1ass Transfer between Phases • • • . • • • • • • • • • • • 4
2. Nolecular l1ass Transport • • • • • • • 6 .3. Diffusion in Binary System • • • • • • 6 4. Separation Based on Mass Transfer • • • 8
c. Theory of Heat Transfer • • • • • • • • • • 8 D. Hechanism of Simultaneous Heat and Nass
Transfer through a Porous, Hater-repellent Hembrane. _ • • • • • • • • • • • 12
E. Jlheoretically Based Equations for Combined :Nass and Heat Transfer • • • • • • • • • 14
I I I • EXPERIIVIEN'l,AL • • • • • • • • • • • • • • • • • 25
25 28 28 28 .30 .32 .32 .34 .36
A. Apparatus • • • • • • • • • • • • • • • • • B. 11aterials • • • • • • • • • • • • • • • • • c. Procedures • • • • • • • • • • • • • • • •
1. :r-rembrane Preparation • • • • • • • • • 2. Experimental Procedure • • • • • • • •
D. Neasurements • • • • • • • • • • • • • • • E. Heat Loss Approximation • • • • • • • • • • F. Nethod of Calculations • • • • • • • • • • G. Data and Results • • • • • • • • • • • • •
IV. DISCUSSION • • • • • • • • • • • • • • • • • • .37
A. Introductory Remarks • • • • • • • • • • • .37 B. f·1embrane Characteristics • • • • • • • • • .38 c. Correlations Developed between the
Experimental Data and Theoretical Equations • • • • • • • • • • • • • • • • .38
1. I1ass Transfer by J.1olecular Diffusion. • .39 2. Heat Transfer by Conduction • • • • • • 46
D. Comparison of Results • • • • • • • • • • • 47 E. I1is cellaneous • • • • • • • • • • • • • • • 54
V. CONCLUSIONS • • • • • • • • • • • • • • • • • • 57
VI. RECOMJVlENDAT IONS • • • • • • • • • • • • • • • • 58
VII.
VIII.
APPEI·JDICES • • • • • • • • • • • • • • • • • • •
Appendix A - Naterials • • • • • • • • • . • • • Appendix B - Hembrane Characteristics and
Data for Heat Loss Approximation • • . • • • • Appendix C - Data and Results •••.••••• Appendix D - Computer Program • • . • • • . Appendix E - Least-squares Approximating
~echl'lique . . . . . . . . . . . . . . . . . . BIBLIOGB...4..PHY • • • • • • • • • • • • • • • • •
IX. ACKNOWLEDGEHENT • • • • • • • • • • • • • • • •
X. vrrA . . . . . . • • • • • • • • • • • • • • • •
v
PAGE
59
60
61 64 74
77
85
87
88
vi
LIST OF FIGURES
FIGURE Fil.GE
2.1 Rea t Conduction through a Wall, Placed betvJ"een Two Fluids of Temperature ts and tf •••••. 10
2.2 Simultaneous Nass and Heat Transfer through
.3.1
4.1
4.2
Porous, Water-repellent IIJ:embrane • • • • • • • . 15
Experimental Apparatus • • • • • • • . • . . • . 26
Reciprocal of Nass Transfer Coefficient versus Fl • • • • • • • • • • . • • • . • • . • 42
Reciprocal of r1ass 'l'ransfer Coefficient Versus F • • • • • • • • • • • • • • . • • • . 43 2
4 • .3 Vapor Pressure of \-later as a Function of
4.4
4.5
'rempera ture • • • • • • • • • • • • • • • • • . 41+
Heat Transfer Coefficient versus F.3
Heat jrransfer Coefficient versus F4
• • • • • . 48
• • • • • • 49
4.6 Experimental Heat Transfer Coefficient versus Heat Transfer Coefficient Calculated fron Equations 4.2 and 4.6 ••••••..•••.. 50
4.7 Experimental Heat Transfer Coefficient versus
4.8
4.9
heat Transfer Coefficient Calculated from Equations 4 • .3 and 4.6 •••••••...... 51
Reciprocal of Hass Transfer Coefficient versus F . . . • • • • • • • • • • • • • • • • . 53 5 Reciprocal of Eass I'ransfer Coefficient versus F6 • • • • • • • • • • • • • • . . . . • 55
vii
LIS'r OF 'l'ABLES
·i..1ABLE PAGE
B.1 r<!embrane Characteristics • • • • • • • • • • • • 62
3.2 Data for Heat Loss Approximation of Apparatus. • 6J
C.1 Data and Results of Run Number 1 b = 0.50 • • • • • • • • • 0 • • • 0 • 0 0 • • • 65
C.2 Data and Results of Run Number 2 b = 0.50 • • • • • • 0 • • • • • • • • • • • • 0 66
Co] Data and Results of Run Number J b = 1.0 • 0 • • • • • • • • • 0 • 0 • • 0 • 0 0 67
c.4 mta and Results of Run Number 4 b = 1.0 • 0 • • • 0 0 • • • • • • • 0 • • • • 0 68
Co5 Data and Results of Run Number 5 b = 2.0 • • • • 0 0 0 • 0 • 0 • 0 0 0 • 0 0 • • 69
c.6 Data and Results of Run Number 6 b = 2.0 • • • • • 0 • • • • • • • • • • • • • 0 70
C.? Data and Results of Run Number 7 b = 4.0 • • • • • • 0 • • • • • • • • 0 • • • • 71
c.s Data and Results of Run Number 8 b = 4.0 • • • • • • • • • • • • • • • • • • • • 72
C.9 Data Used for Least-squares Analysis • • • 0 • . 73
c
Viii
NOHEHCLATURE
A= area of membrane used for mass and heat transfer, ft. 2
b = a variable assumed to represent thickness of the mem
brane, defined as gm. of glass fiber/0.115 ft. 2 standard
area of membrane prepared as described on page 62.
C = total molar concentration of the entire medi~~. lb. moles/ft.J
f = molar concentration of liquid I'Tater on fresh Hater side,
lb. moles/ft. 3
cs = molar concentration of liquid 't'later on salt water side,
lb. moles/ft.J
c1 = molar concentration of water vapor at the membrane surface
on salt water side, lb. moles/ft.J
c2 = molar concentration of water vapor at the membrane surface
on fresh w·ater side, lb. moles/ft. 3
2 DAB = binary gas diffusivity for system A - B, ft. /hr.
D =effective diffusivity, ft. 2/hr. e
E = boiling point elevation of salt solution, °F
HL = enthalpy of liquid 't\Ta ter at its cell inlet temperature,
:Stu./lb.
I~= enthalpy, of saturated water vapor at salt water bulk
temperature, Btu./lb. 2 hs = heat transfer coefficient on salt water side, Btu./ft.
0 hr. F. 2 hf = heat transfer coefficient on fresh water side, Btu./ft.
0 hr. F.
h = assumed heat transfer coefficient for either fresh or
salt water, Btu./ft. 2 hr. °F.
ix
Km = over-all mass transfer coefficient based on the driving
force of partial pressure differences, lb./ft. 2 hr. in. Hg.
k =thermal conductivity of solid, Btu./ft. 2 hr. °F/ft.
ke =effective thermal conductivity of membrane, Btu./ft. 2
hr. °F/ft.
I1A = molecular weight of component A, lb./mole
r,r "B = molecular weight of component B, lb./mole
NA molar flux of component A, lb. 2 2 = moles/ft. hr. or lb./ft. hr.
PT = power input to salt water chamber, watts
PL = heat losses from salt water chamber to surroundings, watts
Ps = equilibrium partial pressure of water vapor on the salt
water side, in. Hg.
pf = equilibrium partial pressure of water vapor on the fresh
water side, in. Hg.
p1 = partial pressure of water vapor on the membrane surface
on salt water side, in. Hg.
p2 = partial pressure of water vapor on the membrane surface
on fresh water side, in. Hg.
qc = flux of heat transfered by conduction through the mem-
2 brane, Btu./ft. hr.
q~ = flux of heat transfered through the liquid film,
2 Btu./ft. hr.
R = gas law constant
'r = absolute trmperature, 0 R. 0 T = average absolute temperature, R.
= bulk temperature of fresh water, °C.
0 room temperature, c. 0 = bulk temperature of salt water, c.
tf = bulle tel11perature of fresh 11ater, oF.
t.,. = bulk temperature 0
of salt v'later, Op
4- = temperature on the membrane surface on salt Hater side, "1
t2 = tenperature on the membrane surface on fresh uater side,
T' = over-all heat transfer coefficient based on only the .J c heat conducted through membrane, Btu./ft. 2 hr. 01:1
.!! •
VA = molecular volume of A, ft.3/mole
v molecular volume of B, 3 = ft. /mole B
\{ = volume of condensate collected, ml.
YA = mole fraction of Hater vapor in membrane pores
YA1 = mole fraction of water vapor on the. surface on salt
~rater side
yAZ = mole fraction of water vapor on the surface on fresh
i'later side
AHv = latent heat of vaporization, Btu./lb.
AP =driving force, (ps - pf), in. Eg.
~t =temperature drop across the membrane, (ts - tr),°F
g = time duration to collect \~ ml. of condensate, seconds
Tr = total pressure, in. Hg.
0.,., .!' •
01.;1 ... .
1
I. INfRCDUCriON
Research in membrane phenomena and theory has a long
history, especially for biological systems. Presently the
application of membranes in engineering is in a state of rapid
development. Processes of separation and purification based
on selective properties of membranes have been found to be of
great potential industrial importance.
Evaporation is the principal industrial method of separa
ting a volatile solvent from a solution containing a non
volatile solute. For example, mineral-bearing water is often
evaporated to give a solid-free product for boiler feed water,
for special process requirement, or for human consumption.
11ulti-effect evaporators are commonly used to increase the econ
omy of evaporators over that of a single effect. Each effect
must normally be at a different pressure in order to obtain
a certain temperature drop across its heating.surface. I'he
Nhole system requires large spaces, and complex equipment.
A stage of flash evaporation requires only a liquid sec
tion, a vapor space and a condensate section,but no heating
surface. With certain flow patterns, a porous l'Tater-repellent
membrane, with solution on one side and condensate on the
other side, can provide an infinitely large number of single
pore "stages". Hm'fever, there exist some disadvantages. I' he
membrane providing the required vapor space produces a resist
ance to the mass transfer of vapor, and also the heat con
ducted through the membrane causes extra heat consumption.
2
For these reasons, a thorough study of mass and heat
transfer relations and their relative Inagnitudes is necessary
before commercializing this process.
The purpose of this investigation is to study the depend
ence of mass and heat transfer properties on temperature dif
ference and membrane thickness, and to study the relationships
between over-all heat transfer coefficients and over-all mass
transfer coefficients.
II. '.rHEORETICAL ANALYSIS
AND
LITERATURE REVIE\-1
J
In this section the relevent literature and theory are
reviewed with regard to membranes, diffusion, heat transfer,
and the mechanism of simultaneous mass and heat transfer
through a porous water-repellent membrane.
A. Hembrane:
A membrane is usually a form of gel with certain struc
tural and permeability characteristics. Gels are colloidal
dispersions consisting of two phases: a solid dispersed phase
and a continuous liquid phase (28). Originally, most of the
membranes used in scientific investigations were natural mate
rials such as animal sacs, fish bladders, and apple skin.
Presently, a variety of materials such as cellulose acetate,
synthetic resin, •reflon, and fiber glass are used in fabrica
ting membranes.
filuch of the historical development of membrane theory
was stimulated by an attempt to explain transport phenomena of
biological systems. During this century, potential separation
processes based on membranes have become an attractive field of
study. Technical progress in dialysis, electrodialysis and
reverse osmosis is in such a state that they are widely applied
in engineering (18, 19), and show much promise for future applica
tion. Recently, Rickles and Friedlander (21), and Findley (4)
have shown the highlights of new features of membrane application.
rhere are two types of membranes 't'rhich may be used in
separation processes. One type is homogeneous and consists
of only one apparent phase on a macroscopic scale. Another
4
type is heterogeneous and consists of more than one phase,
usually a solid phase and either a liquid or a gas phase. Ins ide
the homogeneous membrane, mass transfer by convection or hydrau
lic flow is prevented by the membrane, whereas such mass
transfer may occur inside heterogeneous membranes. Heteroge
neous membranes consisting of glass fiber, reflon, and air
were studied in this investigation.
A porous membrane separating two fluids may possess permi
selectivity or transfer properties which are selective -- i.e.
permit transfer of some components but not of others. Hass
transfer through such membranes is normally by molecular diffu
sion ( 29). 'rhe driving force for this movement is a concentra
tion, thermal, or pressure gradient. Gas or vapor permeates
into the membrane and diffuses through the interstices of pores.
The rate of transfer by molecular diffusion is inversely
proportional to the square root of the molecular weight. rhe
water-repellent properties of the membranes studied served to
prevent liquids from penetrating the pores and thus maintained
the vapor space within the membrane.
B. 'rheory of Nass ·rransfer:
1. Equilibrium and Mass Transfer between Phases:
Equilibrium is the condition for all combinations of
phases such that net interchange of mass and energy is zero.
5
For all combinations not at equilibrium, the difference between
the existing condition and the equilibrium condition is a
driving force, or a potential difference, causing a change of
the system toward the equilibrium condition (5). \'ihen two sub
stances or phases not at equilibrium are brought into contact,
there is a tendency for a change to take place and material
or energy will diffuse from a region of high concentration
(activity) to one of lm'l concentration (activity).
In all mass transfer operations, diffusion occurs in at
least one phase and often in both phases. The mechanism of
diffusion will be discussed later.
In evaporation of solutions, solvent diffuses through the
liquid phase to the interface between phases and then transfers
by diffusion, convection and, or, flow into the vapor phase
from the interface.
The action at the actual interface between the two phases
is important in the diffusion process. It is difficult to
obtain direct evidence of the action at the interface, but
it is commonly assumed that little or no resistance to mass
transfer exists at the interface itself. Goodgame and Sherwood
(7) have demonstrated equilibrium at the interface in one
experimental investigation. For the usual situation of low
and moderate diffusion rates in the individual phase, the
resistance to mass transfer at the interface is probably small.
'rhe relationship of mass transfer at a vapor-liquid interface
to vapor-pressure driving forces has been developed by Knudsen
( 12).
6
2. ~olecular hass Transport:
Molecular transport occurs as a movement of individual
molecules and results in the accompanying transport of mass,
heat and momentum. rhe transport of mass by individual molec-
ular motion is usually refered to as nr,1olecular diffusion".
Sherwood and Pigford (22) defined molecular diffusion as the
spontaneous intermingling of miscible fluids placed in mutual
contact, accomplished without the aid of mechanical mixing.
Diffusion may be induced by a concentration, thermal or pres-
sure gradient, or by other means. rhe most common cause of
diffusion is a concentration gradient of the diffusing campo-
nent. A concentration gradient tends to move the component
in such a direction as to equalize conentration and destroy
' the gradient ( 15). ·rransference of material due to convection
or turbulent mixing is refered to as "eddy diffusion". Eddy
duffusion is much more rapid than molecular diffusion cut
occurs only in spaces rather large compared to the pores of
a membrane.
Diffusion in liquids is fundamentallynot different fro~
diffusion in gases. In theory, the same laHS apply. I·lore
than one hundred years age (1855), Fick proposed a basic empir
ical law of one-dimensional molecular diffusion ( 26), ~'lhich
is widely used in all diffusion problems.
3. Diffusion in Binary System:
Reasoning that diffusion along a concentration gradient
should be governed by a law analogous to Fourier's law of heat
7
conduction along a temperature gradient, Pick deduced that the
molar flux across a phase perpendicular to the direction of
the concentration gradient should be directly proportional to
the concentration gradient. A number of mathematical state
ments of Fickts law have appeared in the literature.
For diffusion in a binary system, Fickts first law in
terms of NA, the molar flux, given by Bird, Stewart and
Lightfoot (1) is:
NA- yA(NA + NB) - CDABVYA (2.1)
\<lhere NA, NB - molar flux of A and B respectively
YA = mole fraction of A
c - total molar density of the entire medium at
some point along path
DAB = proportionality coefficient, or diffusivity
\1 = "gradient" or 11del 11 operator
This equation shows that the molar flux NA is the result of
two vector quantities: the molar flux which results from the
bulk flo.-r, yA (NA + NB), and the molar flux resulting from the
diffusion, CDAB VYA.
Equation 2.1 may be used directly if the system is one
of steady state. But, it is necessary to know the relation
between NA and NB, and to know the analytic expressions for C
and DAB as a function of position or yA in order to obtain a
solution. Since information is usually limited in diffusing
systems, and the resulting equations are not simple, various
averages and approximations are normally used.
4. Separation Based on I'1ass 'rransfer:
For mass transfer from one phase to another, usually
one component of the phase will transfer to a greater ex:tent
than another. 'rhis will cause a separation of the components
of the mixture. Hass transfer properties in separating a
mixture depend upon the phase characteristics, equilibrium
relations and ch.e.m.ical properties of the material to be pro
cessed (6). In a gas-liquid system, if the liquid consists
of a nonvolatile solute and a volatile solvent, mass transfer
of the solvent to the gas phase will cause a complete separa
tion of the solvent from solute. Evaporation is a typical
example of this kind of operation.
Hhen tlf;o liquid phases, one containing volatile compo
nent A and nonvolatile component B and the other containing
pure A, are separated by a water-repellent membrane with gas
filled pores, component A can be separated and transfered
from the solution to the pure A liquid by supplying any driv
ing force which will produce a transfer of A in the vapor
phase.
c. Theory of Heat Transfer:
Local temperature difference causes, in all media, heat
flows such that thermal energy is transported from regions
of high temperature to regions of low temperature. Heat may
flow by one of three basic mechanisms: conduction, convection
and radiation.
In a solid body, the flow of heat is caused by the
transfering of molecular lcinetic energy from molecule to
molecule without appreciable net movement of molecules.
This is called conduction. In liquids, the molecules are
not confined to their locations, but move around and trans-
port kinetic energy in this way as by conduction. So long
as no macroscopic movement can be detected, this process is
still classified as conduction. In practice, heat flol'TS
through thin liquid films are considered as conduction.
Usually macroscopic movements are present in fluids and
9
transport heat by mixing or turbulence. rrhis mechanism is
known as convection. Radiation is a term given to the trans
port of energy by means of electromagnetic waves. In these
experiments, conduction and convection are the important
types of heat transfer.
Consider a special case of heat transfer. In Fig. 2.1
is shown a solid wall separating two fluids. Suppose there
is a device for generating heat in Section I, and a mechan
ical cooler in Section III. In Section I, the temperature of
the heated fluid adjacent to the heater is higher, so its
density is les.s than that of the unheated fluid at a distance
from the heater. The density difference causes some unbalance.
As a result of the unbalanced forces, a circulation is gen
erated and it will bring the fluid to an approximately uniform
temperature, ts• This is the phenomena of natural convection.
In Section III, the same process requires that fluid adjacent
to the cooler has a lower temperature and higher density than
10
Heat Heat in out
qc
ts __,.
t 4-) tr .
G)
~ 4-)
~ CD I II III ~ (Hot fl.uid) (Solid (Cold fluid) CD wall) E-1
Distance, a. .....
Fig. 2.1 Heat Conduction throagh a Wall, Placed between Two Fluids ot Temperature t 8 and tr
11
the bulk o:f the fluid. ·rhe bullr temperature of fluid in
Section III is tf• Two thin stagnant films exist on each
side of the wall. .rhe interfacial temperatures between wall
and fluids are labelled t 1 and t 2 respectively.
Since there exists a temperature difference bet"t'leen the
two fluids, heat ltlill flow from the hot fluid through the
wall to the colder fluid. If the system is one of steady
state, there ~'lould be a constant heat flux, q • ·rhe heat c
transfer at the boundaries z = zl and z = z2 is given by
Net"lton• s "law of cooling" w1 th heat transfer coefficients he "" I
and hf respectively (2), i.e.:
. qc = hs(ts- tl) = hf(~t- tf) (2.2)
Then
t -t -q /h s 1 c s
(2.J)
and
( 2.4)
'rhe heat trans:fer in the solid wall is governed by a well
knotm empirical lal'l deduce.d by Fourier ( J). The one-dimensional
:form of Fourier• s law of heat conduction is
Where qz
k
dt Tz
Then heat
and
---
q z -- k M
dz
heat flux in z direction
thermal conductivity
temperature gradient in z
conduction in a solid wall
q - -k
(2.5)
direction
can be expressed as:
(2.6)
12
(2.7)
Summing up equation 2.3, 2.4 and 2.7
q bqc q ts - tf = __.£ + -k + c
hs hf
= q <L + b + L) c hs k hf
(2.8)
For this type of heat transfer with constant heat flux, it
is customary to employ an over-all heat transfer coefficient
uc' as:
q = u ~t c c ( 2. 9)
L'Jhere q is heat flux and At is over-all temperaure difc
ference, ts - tf.
Comparing equation 2.8 with 2.9
The usual form of the rate equation is:
rate = driving force resistance
(2.10)
Then it can be seen that (ts - tf) is the over-all driving
force, and 1/Uc is the over-all resistance. Equation 2.10
expresses the fact that over-all resistance is the sum of
individual resistances.
D. .Iviechanism of Simultaneous Heat and Nass rransfer through
a Porous, Water-repellent Hembrane:
When a porous, water-repellent membrane, Section II in
Fig. 2.2, page 15, separates two fluids at appropriately dif-
,
13
ferent temperatures; one, fluid I, consisting of volatile
component A and nonvolatile solute, and the other, fluid III,
being condensate of A; the temperature gradient casues a
vapor pressure gradient of A. Under these gradients, mass
and heat will transfer from the high temperature region to
the low temperature region.
Hass is transfered from the hot fluid to the cold by the
following steady state processes:
(i) diffusion from the hot fluid to the membrane surface,
(ii) vaporization at the membrane surface,
(iii) flow or diffusion through pores of the membrane,
(iv) condensation at the membrane surface.
The mass transfered by pDocess (i) is by liquid phase diffu
sion, as has been discussed previously (II. B. J). If non-
condensable gases are present in the pores of the membrane,
process (iii) is essentially gas phase diffusion in a multi
component system. Consider the case in which there is only
one non-condensable gas, say component B, present in the mem-
brane. Then the analysis reduces to a problem of diffusion
in a binary system. For this type of problem, net mass trans
fer is in the z direction only.
Equation 2.1 in one dimension is:
(2.11)
The non-condensable gas, B, stays stationary during pro
cessing, so that NB = 0. Then equation 2.11 becomes
dyA
NA = YA NA - CDAB ~ (2.12)
14
It follows that the molar flux H1, can be exnressed as .. ...
CD dy NA = _ AB A
1-yA dz (2.13)
'rhe mechanism of heat transfer through the membrane is
quite similiar to t>Jhat has been discussed in II. c., except
some additional effects have to be considered. 'rhese are:
first, heat is conducted through not only solid membrane,
but also the pores in the membrane; second, the diffusing
vapors will be accompanied by their latent heat of vaporiza
tion which will be transfered to the colder fluid upon
condensation. 'rhe conduction of heat in a gas, where there
is diffusion in the direction of heat flow, is greater than
if the gas were stagnant (23). In developing heat transfer
equations later, the concept of an effective thermal con
ductivity, ke, which combines the complex conduction and
transport mechanism, will be introduced. The heat conduction
through the membrane may be written as:
(2.14)
Hhere q is heat flux through membrane by conduction and b c
is the thickness of the membrane.
Note that the rate of heat transfer through films does
not equal to q , but it includes in addition the latent heat c
associated with mass transfer.
E. Theoretically Based EqUation for Combined ~mss and Heat
Transfer:
Mass transfer between phases involves diffusional
I
I r (Hot Solutn)
'remp. t s
Equil. Ps
Liq. Cs
Equil. Vapor ·- - Cone-:- - - - r· -
I
I
II (Membrane)
b
r III I (Cold Condensate) I
tr
cr
Pr
I I
, __ 1 Equ11. Vapor ----·------1 Cone.
Fig. 2.2 S1multaaeo•• Mass aad Heat Transfer through Porous. Water-repellent Membrane
15
16
resistances in series. These diffusional resistances are
additive l·Ihen the mass transfer flux is constant along the
diffusion path at steady state. As shown in Fig. 2.2, the
diffusing component, A, has to face four resistances: a solu-
tion liquid film resistance on hot solution side, two inter-
facial resistances and a diffusion resistance in the membrane
pores. For low and moderate diffusion rates, the resistance
at the interface is. probably small and will be neglected in
most cases (16). Compared to resistance exerted by the men-
brane, liquid film resistance is assumed negligible.
In this particular investigation, the diffusing compo
nent, A, and non-condensable gas, B, as discussed in II.D.
are water and air resp~ctively.
Equation 2.13 states that
CDAB dyA NA = - 1-YA dz
The system is at steady state and of constant crossectional
area along the transfer path, so
-dz = 0
Differentiating equation 2.13 with respect to Z
d CD dy - ( AB --l!) = 0 dz 1-YA dz
Since the diffusion path and area are not knoi'm, and since
adsorption and desorption might occur in the membrane pores,
it is necessary to define an effective diffusivity, De, to
replace the formallY defined diffusivity, DAB, for gas pairs.
17
Rewritten, the above equation is
d (CDe dyA) = O dz 1-y dz (2.15)
A
At moderate temperatures and pressures, the ideal gas law
holds for water vapor and air mixtures, so, the total con
centration is:
c = rr Rr
Where rr = total pressure
R - gas constant
T - absolute temperature
The gas di~fusivity of a binary t i .L gas sys em g ven by Naxwell,
Jeans, and Champman is (24):
·r3/2 JFf D - d - k
AB - ff(V 1/3 + V 1/))2 . A B - 1 A B
Where d is numerical constant
VA, VB - molecular volume of A, and B (25)
MA, MB - molecular weight of A, and B.· Letting
d 1 k1 = ( 1/3 1/3)2
- , a constant for a JliB
VA + VB certain pair of gases.
product of C and De
.IT.. k rr3/2 = CDe - RT 1 1t
Where k 2 is a constant.
can be expressed as:
(2.16)
In these experiments on water vapor transfer through porous
membranes, the temperature difference between salt and fresh
water sides is less than 30°F., so it is reasonable to consider
CDe as a constant and having the value of ,_ CDe = k2 ~T
18
(2.17)
Where r is the arithmetic average absolute temperature in the
membrane. rrhen equation 2.13 and 2.-15 become:
k fF dy N = - 2 __J};.
A 1-yA dz (2.18)
k ~ _ddz ( 1 dyA) = o 2 ~ l. 1-yA dz
or
1 dy. £..... ( ~) = 0 dz 1-YA dz
(2.19)
The above differential equation is to be solved with the
following boundary conditions:
B. C. 1: at z
B. C. 2: at z = b, YA
Integrating equation 2.19 gives
- ln(1 - yA) = k 3z + k4
Applying the boundary conditions,
1 1 -YA1 k 3 = b ln
1-YA2
k 4 =-ln(1 - YA1 )
Substitute equations 2.21 and 2.22 into 2.20
z 1-YA - ln(1 - yA) = -b ln 1 - ln(1-YA1)
1-YA2
Rearranging the above equation gives
( 1 ) ( 1-YAz z/b 1 - YA = - YA1 )
1-YA1
On differentiating equation 2.23,
dy 1-~2 z /b ( 1-YA2) 1 - dzA = (1-YA1) (1-YA1) ln i-yA1 b
(2.20)
(2.21)
(2.22)
(2.23)
Combining with equation 2.23
dy A
- -= dz
Substituting equation 2.24 into equation 2.18, gives
IT 1-yA2 NA = 1c2 ln 1 b. -YAl
19
( 2. 24)
(2.2.5)
All these experiments were investigated under atmospheric
pressure, so the vapor-air mixture was inside the ideal-gas
region. 'rhen
:1. -lf and
Rewriting equation 2.25 in partial pressure form and taking
Naclaurin series expansion in order to obtain a form suitable
for linear least-squares analysis,
(2.26)
vlhere n = 1 , 2 , 3 , .• • • , GO
By neglecting terms of order higher than 2
(2.27)
20
Equation 2.27 sho~Ts mass transfer flux is a function of mem-
brane thickness, interfacial partial pressure of water vapor,
average temperature and operating pressure. Since interfacial
temperatures and their corresponding partial pressures are
not known, some modification has to be made to equation 2.27
in order to obtain an applicable equation.
'rotal heat transfered from hot fluid to cold is the sum
of heat transfered as vapor latent heat, qv, and heat con
ducted through the membrane, qc. 'rhis heat will flow through
both films on each side of the membrane.
l'here:f'ore
(2.28)
(2.29)
Assuming equal film heat transfer coefficients on both sides
of the membrane. hs =. hf = h.
·rhen
If AI-lv
Equation
Hence
t -s
is the
q = v
2.14
tl = t2 - tf = latent
N A .t..H.v states
k e
heat of
=-b
qv + qc
h (2.30)
vaporization, then
(2.31)
(2.32)
rrh t difference between the two fluids e over-all tempera ure
21
is the sum of the individual temperature drops across the two
liquid films and the membrane, i.e.:
ts - tf = (ts - tl) + (tl - t2) + (t2 - tf)
Substituting equation 2.3~ into 2.)) gives
2 2ke ts - tf = h NA AHv +""bh(tl - t2) + (t1 - t2)
(2.33)
= ~ NAAliv + (~ + 1)(t1 ~ t 2 ) (2.34)
For moderate temperature differences, (ts - tf), it seems
reasonable to assume that
P1 + P2 ~ Ps + Pf
and (t1 - t 2 )/(ts - tf) ~ (p1 - P2)/(ps - Pf)
By these assumptions equations 2.34 and 2.27 can be expressed
as
or
(2.36)
And then from equation 2.)5, by substitution for (pl - P2 ),
2 2ke ts - tf) (.!L) ( J;) x ts - tf = h NA~Hv + (hb + 1)(Ps - Pf k2 .JT
NA (----)
Ps + Pf 1 +---211"'
t 8 - tf (2 Ps - Pf = NA ( P p ) h ( t - t ) ~Hv
s - f s f
2 2ke ...:E ,r J + i;(h'b"" + 1 ) If 21f+ P8 + Pr
(2.)7)
22
If w·e define an over-all mass transfer coefficient as follows:
NA = Km(Ps - Pf) = Km AP
Where /;lp = p - p s f
(2.J8)
Then, by combining equation 2.37 and 2.J8 and rearranging, the follov{ing equation t·rould be applicable:
1 2 (Ps - p 2 2ke lr2 = f)ARv b
h +- (- + 1)-ISn ts - tf kz hb JT2IT+ Ps + Pr
2 (Ps - Pf) till 4ke 1T'2 = Fi +-ts
v k2h (2Tf + Ps + Pr)/T - tf
2 1r2b + -k (2lt + 2 Ps + Pf)JT:
(2)~A 4ke 1T2 2 IT 2b = Fi ~t Hv + (k2h) ( 21f + Ps + Pf) .[T +( k2) ( 2Tr + Ps + pf) J¥
(2.J9) 1dhere AP = p s - p f , and ll t = t s - tf
The terms in parentheses are assumed approximately constant
in equation 2.39, and are in a form suitable for determination
as least squares coefficients of the parameters,
In this particular investigation, an important variable
is the membrane heat loss - heat transfered through the mem-
brane by conductfon, q • Since interfacial temperatures t 1 c and t 2 can not be directly measured, equation 2.14 is not prac-
tically applicable. For this reason, defining an over-all heat
transfer coefficient based on over-all temperature difference
is desirable.
23
Define over-all heat transfer coefficient, uc, according to
qc = Uc(ts - tf) = UcAt
Equation 2.14 states
1 b At -
(2.40)
u0 ke t 1 - t 2 (2.41)
From equation 2.34 and 2.38, we can get the following relation
2ke 2ke -+1 -+1
1 hb hb ------- - -------------- = ----------------t1 - t 2 2 2 A
At - h N A AH.v At - h Kin up Llliv
1 -At 1
2ke -+ 1 hb
- 2~~LU!v h At
By combining equation 2.41 and 2.42,
2k 2 b e + 1 h + ke L = ~ __ h_'E ____ - -------
uc Ke 2K A p 2 A P 1 T ~ t ~Hv 1 - h ~ A t A~
(2.42)
'rhe liquid film heat trans:fer coe:fficient is much larger than
the membrane effective conductivity-- b/ke>> 2/h, so we elim
inate the term 2/h in the numerator of above equation without
introducing signi:ficant dif:ference. Then
b
1 Ka - --------~-----~ - 1- ~ K AE4Ey
h.in ~t
24
or
(2.43)
Here, also, the terms in parentheses are assumed approximately
constant and can be determined as least square coerficients
of the parameters:
1 b ,
In this investigation, the hot liquid used was 7% salt
solution. A 7% salt solution was calculated to have an ac
tivity of water of o. 96. The cold liquid ~1as water condensate,
therefore:
Ps - 0.96 x (vapor pressure at ts)
Pr - vapor pressure at tf
This analysis suggests an experiment should measure water
mass transfer across membrane of various thickness as a func-
tion of bulk liquid temperature difference. These measurements
would provide values for the fundamental transport coefficients
for this process.
25
III. EXPERIHENTAL
A . Apparatus :
The apparatus used for this investigation consisted of
two chambers 2-1/8 inches in diameter formed by sections of
plastic pipe 1-1/2 inches thick with a membrane between them,
two electric heaters - one in the salt water section and the
other in the fresh water section, rubber gasketing, and the
necessary measuring devices. The plastic shells of the cham
bers had holes for inserting heaters, filling tubes and vents.
Thermocouples were inserted through holes in two of the rubber
gaskets. The whole assembly was clamped together by two steel
flanges and four long bolts, and was covered with glass wool
for the purpose of insulation. The apparatus is illustrated
in Fig. 3.1, and its major components are described below:
'l'he I1embrane {Ivi): This is a porous, water-repellent membrane
made from fiber glass and Teflon. The Teflon imparts the
water-repellent character to the membrane. This property of
the membrane allows only water vapor to pass through the pores
and retains liquid at membrane surfaces. Membranes of four
different thickness were prepared for this investigation. The
detailed method of preparing the membranes will be discussed
later.
The Electric Heaters (H1 , H2 ): The electric heater in the salt
water section is the source of energy for evaporating the salt
water. 1'he other one, in the fresh water section, was used
to control the coolant temperature. Both heaters were made
26
Fig. ).1 Experimental Apparatus
A B1,B2 C1,C2 o,.,P2 E1,E2 F1,F2 G1,G2 GJ,G4 J M p R s1.s2 T1,T2 v1,v2 w z
Aa-bestos Vents Chambers for Salt and Fresh water Make up Line• Fresh Water outlet Steel F~es RUbber a.aket tor Inserting Thermocouples Rubber Gasket for Sealing Graduated cylinder ••bran• Pote~t1o:tneter :Reserto1r Plast1o Shells The:NDoouples variacs Wattmeter Plastic Plate
27
by inserting wound nichcrome wire into bent Pyrex glass tubes.
The Plastic Shells (s1 , s2 ): Two plastic shells with inside
diameter of 2-1/8 inches, separated by two rubber gaskets (G1
and G2 ) and membrane (M), created two chambers (c1 and c2 )
required for containing the salt water and fresh water respec
tively. Holes were drilled to insert heaters (H1 and H2 ) and
tubings (B1 , B2 , n2 and E2 ). PVC plastic was used due to its
low heat conductivity, ease of fabrication, and availability.
I'he Plastic Plates and Asbestos (Z, A): The plate (Z) was
plastic 1/4 inch thick. It served to cover the salt water
chamber (c1 ), and also, having asbestos (A) between it and the
flange (F1 ), to reduce the heat loss.
'rhe 'rhermocouples (Tl, T2 ): rrwo Copper-Constantan ther
mocouples were used,one on each side of the membrane. They
were placed right adjacent to the membrane surface, and the
measurements were considered to be bulk temperatures of salt
and fresh waters.
The ~va ter Reservoir ( R): 'rhe object of this reservoir was to
supply make up fresh water to the salt water chamber in order
to maintain the salt water concentration constant throughout
a run. It is a plastic container.
'rhe Variacs cv1 , v 2 ): Two "Adjust-a-Vel t" variacs were used
to adjust the power inputs to the electric heaters. Both were
made by Standard Electric Product Co., and had a range of 0-
140 volts.
28
'rhe Hattmeter (Vl): A wattmeter was used during this investiga
tion to measure the power input to the electric heaters (H1 ).
It is an A-C and D-C wattmeter made by the Weston Electric
Instrument Co ••
'rhe Potentiometer (P): A potentiometer was used to measure
the e.m.f. of the thermocouples (T1 and Tz) in millivolts.
After conversion to temperature units, it gives bulk tem
peratures of salt and fresh waters.
'rhe Graduated Cylinders ( J) : The graduated cylinders were
used to collect and measure the amount of condensate which
was formed during the run. They were 10.0 ml. and 25.0 ml.
Pyrex glass cylinders.
Hiscellaneous: An electric stirrer, a hot plate and an oven
were used for preparing the membranes.
B. Materials:
The materials used in this investigation, their specifica
tion, manufacturers or suppliers and uses are listed in
Appendix A, page 60.
C • Procedures :
1. Membrane Preparation: Membranes were prepared based on
a Standard "1 gram" membrane containing 1 gram of glass fiber
for a membrane 0.115 ft: in area. Such a membrane was prepared
in the following manners.
one gram of owens-Corning Fiberglas, type AA, 1 micron
29
in diameter, was weighed. About 1/2 of this glass fiber was
crushed with ordinary pliers to reduce the average fiber length.
The rest of the glass fiber was split into small pieces by
hand and placed in a plastic container which contained about
350 ml. of tap water. rhe purpose of crushing the glass fiber
is to improve the uniformity of the membrane. Five drops of
glacial acetic acid was added to acidify the mixture and to
make the glass fiber disperse easily. The contents were then
stirred 1qith an electric stirrer until a satisfactory disper
sion occured. 'rhen 0.5 ml. of DuPont Teflon 30 B aqueous
dispersion was added to the above contents and mixed with the
stirrer for about ten minutes. The Teflon provides a water-
repellent property to the membrane. Then, about 5 ml. of
alumium sulfate (Alz(S04) 3J solution, 0.05 gram per ml. of
solution, were added, again stirring for about ten minutes.
The intended purpose of the alum is to cause coagulation of
'reflon. onto the glass fiber surface. Experiments have verified
its beneficial effects ( 9). ·rhe slurry thus formed \'las ready
for filtration.
·rhe slurry was then filtered by vacuum through a Buchner
funnel, 4.7 inches in diameter, and the filtrate was refiltered
through the glass fiber once again. ·The wet membrane formed
1-vas washed with distilled water before it was removed from
the funnel. Then it was placed in between sheets of paper
towels and rolled with a cylindrical steel pipe to remove most
of the water and to increase the density • The membrane t'fas
then allowed to air dry ~turallY at room temperature for
more than twelve hours. ·rhe · membrane was dried further by
heating between aluminum foil on a hot plate at low heat
setting and was pressed heavily with a wooden block.
)0
Finally, the membrane, which was dried as indicated above,
was heated on an oven at abo.ut 600°F. for 30 minutes approx
imately. reflon is partially melted under this temperature,
so this baking served to combine the ·reflon particles and to
bond them to the glass fiber. It also provides membranes with
more strength. The membrane thus prepared was tested with
cold water as well as boiling water. If the membrane was
sufficiently water-repellent, then it was used in experiments.
During this investigation, membranes of four different
thickness were prepared by using all quantities in proportion
to the standard "1 gram" membrane. The same procedure was
followed in all cases. The materials used for making the
membrane are listed in Appendix A, page6o.
2. Experimental Procedure: The following is the procedure
used during making a run for one single membrane of any
thickness at a particular power input. The experimental
sketch is shown in Fig. ).1 and discussed under the section
of "Apparatus". To begin a run, 7% by weight sodium chloride
solution was filled through tubing n2 into salt water chamber
c1 • This replaced the air in the chamber. Then, the end of
tubing n2 was connected to the reservoir outlet tubing D1.
This permitted water transfer out of the salt water side to
be made up by fresh water, thus maintaining the concentration
31
constant. Salt water level was kept about 1/4 inch high in
vent B1 • Similarly, condensate (fresh water) chamber c2 was
filled with distilled water using tubing E2 until water was
visible in vent B2. This would remove air in the chamber c2 .
After connecting E2 to E1 , distilled water was again fed into
vent B2 until there was water coming out of the tip of tubing
E1. 'rhe tip of tubing E1 as well as fresh water level in vent
B2 were usually about 1/4 inch higher than the salt water
level. This ad·justment of levels was to make sure that the
flow of water out of tubing E1 was definitely due to evapora
tion of hot salt water and not due to leakage of salt water
from chamber cl.
After the le~el adjustment, heating was started. The
electric heater H1 was used to heat up salt water, and the
desired power input was adjusted with the aid of a variac,
V1• The power input was indicated by the wattmeter W. Since
high temperature difference between salt and fresh waters
might cause internal condensation and spoil the membrane,
another electric heater H2 was used to control the desired
temperature of the fresh water side. The variac Vz was used
to adjust power input to the heater H2. Sufficient time
allowance was given to obtain a steady state, which was in
dicated by constant values of temperatures. Heasurements
were then started on condensate outflow rate, temperatures of
salt and fresh waters, room temperature, power input to salt
water, and time. A measuring cylinder J was placed under the
tip of tubing El to collect and measure the condensate.
32
'rhe fresh water was checked i'tTith silver nitrate occa
sionaly to determine whether or not appreciable chloride ions
were present, and if so, the run was discarded. The procedure
was to take 5 ml. of condensate collected and add J drops of
1 N silver nitrate solution, then it was compared to the
turbidity of' 5 ml. of 200 ppm salt solution with the same
amount of silver nitrate added.
Readings were taken for eight different membranes of four
different thickness at different power settings. A minimum
of four reproducible readings were taken at each power setting
during the runs. The membrane characteristics are listed in
Appendix B, rable B.1, page 62.
The power inputs were changed according to the require
ments, by adjustment o~ the variacs v1 and v2 , and the proce
dure o~ taking the readings was repeated after a new steady
state was achieved.
D. Neasurements:
Experimental measurements during each run were teo
peratures on each side of the membrane, room temperature,
power input to the salt water chamber, volume of condensate
collected and time.
E. Heat Loss Approximation:
Although experimental apparatus was covered by glass wool
for t ~ the heat supplied to the salt water insulation, par o~
di i I n order to calculate chamber was lost to the surroun ng a r.
JJ
the amount of heat conducted through the membrane, an estimate
of the heat loss is required. One set of runs was made for
this purpose.
The apparatus 1-was assembled in the same way as shown in
Fig. 3.1 except that a piece of rubber gasket, 0.30 em. in
thickness, was used to replace the membrane, and an analogous
procedure ~;as followed as described in III. c. 2. I11easure-
ments were taken on power input to salt water chamber, tem-
pera tures of salt and fresh waters, and room temperature. I' he
dataare tabulated in Table B.2, Appendix B, page 63.
Since there was no mass transfer, all the pol'ler input to
the salt water chamber flowed out of the chamber - part of it
was lost to the surroundings and the rest of it was conducted
through the rubber gasket to the fresh water chamber. By
applying the least-squares approximating technique, the best
correlation obtained was
P = 0.0548(tcs - t 0 r) + 0.0950(t0 s - tcf)
Standard deviation of error = 0.1379
\vhere p _ power input to salt water chamber, watts 0
- temperature of salt water, C.
t oc. - temperature of fresh wa er, 0
- room temperature, C
(J.1)
I'he part of the heat that was conducted through the rubber
gasket to the fresh water side should be deducted from equation
3.1 to get the amount of heat lost to the surroundings. The
thermal conductivity of rubber was assumed to be 0.10 Btu./
hr. ft. 2 oF./ft. (14), which is equivalent to 0.00173 watt/em. 0 c.'
J4
The area of conduction was 0. 0246 ft. 2 or 22.9 em. 2. ·rhen the
rate of heat conduction through the rubber gasket to fresh
v-,ra ter chamber, Pc watts, is
p = 0.001~~ - 22.9(t - tcf) c O.J X cs
- 0.1.32(tcs - tcf) (.3.2)
Substracting equation .3.2 from equation .3.1, gives
PL = 0.0548(t - t ) - O.OJ70(t - t ) (J.J) cs cr cs cf
where PL - pow·er loss to the surroundings, 't'ia tts.
F. Hethod of Calculation:
The following steps explain how experimental data were
used to calculate over-all mass and heat transfer coeff1-
cients for any membrane thickness at a single power level to
the salt water side.
2 '}lhe total heat flux, <tr Btu./hr. ft. , 't<Tas calculated
from the follo't<Ting equation.
qT = (PT - PL) x J.41J/A
't'Ihere PT _ po't'ler· input to salt water chamber, watts
PL - po't'ler loss to the surrounQ.ings, from equation J.J,
l'J'atts 2
A - transfer area of the membrane = 0.0246 ft. 2
The flux of water, NA lb./hr. ft. is calculated from the
amount of condensate as follow:
NA = 3600 W/(454 SA)
Where w - volume of condensate collected, ml.
35
A- membrane area in ft. 2
e - time duration to collect W ml. of condensate in
seconds
The amount of heat i d f requ re or vaporization through the mem-
brane, qv Btu./hr. ft. 2 , was determined as follow
qv = NA (Hv - HL)
where I~ - enthalpy of saturated water vapor at the salt
water temperature, Btu./lb.
HL - enthalpy of liquid water at its inlet (room) tem
perature, Btu./lb.
'rhe amount of heat conducted through the membrane, q Btu./ c
2 hr. ft. , was calculated as follows:
qc = qT - ~
The over-all heat transfer coefficient based on conduction, 2 0 Uc Btu./hr. ft. F., was evaluated from the equation
Uc = qc/(ts - tf)
l'lhere ts = temperature of salt water, 0 F.
:rhe mass transfer rates were related to vapor pressure dif
ferences across the membrane. An over-all mass transfer coeffi-
cient, K , was used as a measure of mass transfer rates. The m
vapor pressures were calculated separately as follo~rs:
p = partial pressure of water vapor on the salt water s
side
_ vapor pressure in in. Hg. of pure water at ts x0.96,
't-lhere o. 96 was used as ac ti vi ty of water in the salt
solution.
pf _ partial pressure of water vapor on the fresh water
side
36
= vapor pressure of pure water at tf, in. Hg.
The over-all mass transfer coefficient, ISn. lb./hr. ft. 21n. Hg.,
is
G. Data and Results:
All the data taken during the investigation and the
results calculated from the data are tabulated in Table C.l
through C.8, Appendix C, page 65 through 72.
J7
IV. DISCUSSION
A. Introductory Remarks:
In this study of mass and heat transfer through porous,
water-repellent membranes, the object has been to investigate
mass and heat transfer coefficients, their dependence on mem
brane thickness and temperatures, and the relationship between
the two types of transfer. As sho~m on page 22 and 2J, equa
tion 2.38 and 2.40 state that
NA = JSn AP
and
qc = Uc At
Based on these relationships, correlations of the coefficients,
KJn and Uc, have been developed for expe.rimental data.
During this investigation, temperatures of salt and fresh
waters, membrane thickness and power supplied to salt water
chamber 1'lere considered as independent variables. 'l)he volume
of condensate collected per unit time and the amount of heat
conducted through the membrane were categorized as dependent
variables.
For run number 3, an additional rubber gasket was placed
between gasket G4 and flange Fz in Fig. ).1 to keep fresh
Water from contact with the flange. Also there was no power
input to the heater Hz, and the data were used in calculating
mass transfer coefficients only.
The data and correlation deve~oped by a previous author
(20) were used to check the consistency of the results.
38
B. J:Iembrane Characteristics:
The membranes used in this investigation were prepared
by using all quantities in proportion to the standard "1 gram"
membrane as described in III. C.1. The data tabulated in
Table, B.l, Appendix B, on thickness, density, and weight per
unit area o~ membrane were taken on the portion of the membrane
used ~or mass and heat trans~er experiments,, t-lh1ch were some
't'J'hat thicker than the edges cut off. The membranes were not
completely uniform in thickness, and the thickness measurements
depend on the degree of compression during measuring. Thus,
the most reliable measured characteristics related to membrane
thickness were the quantities used in making up the membranes.
In this experiment, the make up weight of glass fiber
was used as a measure of thickness and was defined as the va-
riable b, where 2
b = weight of glass fiber in gra.ms per 0.115 ft.
of membrane.
J1embranes of b = 0.5, 1.0, 2.0 and 4.0 were used in this
investigation. This variable was used in all correlations as
the independent variable representing a measure of thickness,
or more accurately, a measure of thickness times density.
The experimental mass and heat transfer area was
2 0.0246 ft.
c. between the Experimental Data and Correlations Developed -
Theoretical Equations:
At each combination of membrane and power setting, at
39
least 4 replicate sets of data were talren. I d t .... n or er o s im-
plify the least-squares analysis one set of data (which was
already available on a data card) was used to represent each
combination of membrane and power setting. This set of data
i'ras the set having ISn_ and Uc values nearest to the average
for the particular conditions. This data is given in Table C.9,
Appendix c.
The experimental data and results were analyzed by using
the least-squares approximating technique. The aim of least-
squares approximation was to minimize the sum of the squares
of the differences between experimental dependent variable
values and the approximation equation values for the dependent
variable in terms of the desired independent variable parameter~.
Let 1,2, ••• , n be a sequence of parameters
defined for values of independent variables. ·rhe object is
to approximate dependent variable Y by a linear combination
of the \xj1
With the values of Bj, constants, to be determined. In order
to compare the variances of the errors, the form of the depend
ent variable was maintained in most of the analyses attempted.
These dependent variable forms were 1/Km and Uc in this investiga-
tion.
1. Hass Transfer by I'Iolecular Diffusion:
Equation 2 • .39 derived previoUSlY for 1/~ is
40
( 4.1)
Hhere terms in parentheses are assumed approximately constants
and are in forms suitable for determination 1 as east-squares
coefficients of the following parameters:
AP AH rr 2 rr 2b .6 t ~..;). v '
(2IT+ Ps + pf)./T, (2fT+ Ps + Pr)/¥.
I1he equation obtained by least-squares analysis "based on the
above parameters was as follows
1 AP 2 -- o.oo4J5- a~+ z.sz --~n __ _ Km At (2 fr+ Ps + Pr){F
Standard deviation of error = SE = 0.5406
This equation is shown in Fig. 4.1.
( 4. 2)
Comparing the first term of equation 4.2 to that of equa
tion 4.1, the liquid film heat transfer coefficient, h, should
be about 460 Btu./ft. 2 hr. °F. Findley, in previous experi
ments, glued a thermocouple on the membrane surface to measure
the interfacial temperature and obtained data indicating a value
of h of approximately 500 Btu./ft. 2 hr. °F. Further, comparing
the second and the third terms of equation 4.2 to those of eq~a
tion 4.1, it shows that kz and ke have the values of 0.74J and
215. The average density and thickness of membranes are 0.226 gm./
cm.J and 0.00188 ft. per gram of make up glass fiber, respectively.
41
Then the value of' effective thermal conductivity is 215 x
0.00188 = 0.404 Btu./ft. 2 hr. °F/ft •• The composition of the
membrane and vapor space was used to estimate an average ther
mal conductivity of 0.0575, using values of thermal conductiv
ity l'reighted according to the volume fractions (see Appendix B).
The value of lr2 obtained 'tl;as used with equation 2.17 to deter-.... 0
mine De l'Ti th T = 492 R. This value of De after converting
units of thickness to feet proved to be 0.62 ft. 2/hr.. ·rhis
compares well 'N'ith.a value of 0.78 ft. 2/hr. at 492°R estimated
from the value in the literature (17) times the void fraction
of 0.91. This deviation of 20% is believed to be quite rea
sonable in view· of the torturous path through which diffusion
occurs.
1rhe agreement between values of De and h obtained from
the least-squares equation, and those estimated from the com
position and previous experiments appears to be sufficient
to confirm the mechanism of diffusion as the rate controlling
factor. It is possible that the deviation of the ke value
could be attributed to small errors in the rate of conde1wate
accumulation, or to other experimental errors.
Rao {20) in his thesis pointed out that b( Cl..t - E)' l'There
E is the boiling point elevation, has a strong effect on over
all mass transfer resistance. 1/~· Modifying equation 4.1
by adding a parameter, b( ~ t _ E)/ T, where T is average
absolute temperature and E is 1.4, the following equation was
obtained
. ,.0 r-1
' . {:{) f-ri ........ . s.:: ..;
N . .J.) CH
• H ~
~I~
42
10
LEGEND
0: 0 • 5 f'Iembrane ...
.&.= 1.0 Membrane
s: 2.0 Membrane
Y: 4.0 Membrane • .....
.3
2
1
0 2 5 7 9 10
Fig. 4.1 Bectprooal of MaSs TrN&t~1"er Coefficient vs . F 1
AP . 1r 2 F1 • O. G-J.S "n Afl.y + 2.52 (Z·lr+ p + P ) l"f
• r
·Tr2s + 2.69 , see equation 4.2 {21f+ P• + •r>l'f
43
10
LEGEND
0: 0.5 l~embrane 8 8: 1 • 0 lllembrane .
..c El: 2.0 Nembrane r-1 7 ' • tC Y: 4. o r~rembrane ~
• 6 ~ .,...
C\l 5 • .J.) ft.t
• 4 E ..
"I~ J
2
1
0
Fig. 4.2 Reciprocal of Mass Transfer Coefficient vs. F2
P2 • o. Oo42S '}~AlLy + ·3. !6 Tt' 2 .u (2TI+ p8 + Pr)JT
b( 4 t - 1.4) 2 + 0.939. . . Jf b + 24-.3
(2TT+ P~ + Pr)ff
see equation 4.3
44
1 -= y~
o. 00425 ~~ Aliv + 3.16 TT 2 (21{+ p + p )JT s f ".l..
SE = 0.3970
'I' his equation is shown in Fig. 4. 2. The reduction in SE in
equation 4.3 compared to equation 4.2 is barely significant
(4.J
to the 5% probability level, but comparing Fig. 4.1 to Fig. 4.2,
the improvement does not appear to justify the extra term.
Perhaps the improvement is due to a systematic experimental
error or to some modifying factor of minor importance.
A number of other parameters were tried by such techniques,
but they did not tend to reduce the residual variance.
Findley (4), 'ranna (27), and Rao (20) have shown that
there might be a tendency to produce internal condensation
at high values of At. Fig. 4. 3 shows that conditions l'Ti th
a large ~t would more probably involve saturated vapor condi
tions inside the membrane. In Fig. 4.3, ts and tf are salt
and fresh water temperatures. If partial pressure and tem
perature vary linearly with thickness through the membrane,
the condition within the membrane, represented by the line
from t to t ~would come much closer or cross saturation s f>'
conditions in the case of larger At values than in a run
With small~t values. It is also shown in Fig. 4.J that,
at higher operating temperature, a higherAt is endurable
Without causing internal condensation. Internal condensation
might cause a continuous liquid channel through the membrane,
. til ~
. ~ ...... ..
A .. ,...
Q)
+> C\1
:::=:::
G-1 0
Q)
t-1 ;:s I'll I'll Q)
f-1 P-t
f.; 0 A
~ 6
5
I I
... ~t=1o ~ I k bt•15 ~ I
4 130 160 170 140 150
Temperature, t, op
Fig. 4.) Vapor Pressure of water as a Function of
Temperature ( 1 0)
180
46
and it would probably increase membrane heat conductivity,
ke• Also an additional mass transfer resistance would arise
as a result of the occurence of condensation and re-evaporation
from droplets blocking membrane pores. Fig. 4.1 and 4.2 sho\-1
that the experimental results agree fairly "t'lell l'li th the assump
tion that mass transfer through the membrane is by molecular
diffusion.
2. Heat Trans fer by Conduction:
Equation 2.43 derived previously for Uc is
(4.4)
'rhe equation obtained by least-squares approximation based on
the parameters 1/b and Km ll P ~H was b :a:c v
1 Km /).P (4 5) U0 = 15.6 b - 0. 0912 b "1\taHV •
SE - 4.878
and it is shown in Fig. 4.4.
According to equation 4.5, the value of ke should be 15.6
Which is considerably different from the ke of 215 obtained
from equation 4,2. In addition, it is obVious from Fig. 4.4
that the fit of the data would be much better if an empirical
constant or another parameter were included in the results.
Even with another constant the data do not indicate the agree-
4 For this reason, and the presence ment obtained in Fig. .1. f elt that the above of more possibilities for error, it iS
equation does not adequately represent the heat transfer by
h is necessary for conduction, and that an empirical approac
best fit. Investigation l'ias made of several semi-empirical
parameters, and the best approximating equation obtained 't';as
Uc - 9.20 t - 0.0627 5!! AP Aflv + 6.58 b At
S-r.- - 2. 822 l!,
( 4. 6)
and it is shown in Fig. 4.5. Probably the following five
reasons can explain the errors in the correlation for Uc:
(i) internal condensation affects the value of ke,
(ii) ke might be a variable instead of a constant,
depending upon temperature and vapor phase composi-
tion,
(iii) the heat losses approximation given by equation
J.J might not be accurate, or the heat loss relation-
ship may have varied, possibly with air circulation
conditions,
(iv) errors in experimental Km values used in the correla-
tions would cause errors in Uc values,
(v) latent heat of vaporization is very high, a small
error introduced in measurement of condensate
would cause large effect on the value of De·
Comparisons are made for the values of experimental Uc to
those calculated entirely from experimental conditions - i.e.
calculating KID from equation 4.2 and 4.J, then calculati:r..g De
from equation 4.6 using calculated values of Km• They are
Shown in Fig. 4.6 and 4.7. Figures 4.5, 4.6, and 4.7 all
seem to be quite similar.
D. Comparison of Results:
Two groups of experiments have been performed before, on
48
LEGElJD
0: 0.5 Hembrane
A: 1.0 f·1embrane
G.: 2.0 Hembrane
Y: 4.0 r·1embrane
~ 20
0 . ,_, ~
(\1 0 0 .
.p ~
' • ::s .p ~
.. 0
::>
0 10 20 )0
F1g. 4.4 Heat ·rranster coettioient vs. FJ
1 Klr,.AP F; .. 15.6 b - 0,0912-b' ~Ally , see equation 4.5
JO LEGEND
0 . 0.5 l'Iembra.ne . A . 1.0 Nembrane . [!] . 2.0 l·Iembrane .
r:y •= 4.0 Nembrane 0 0
. H ..c G
(\j . .p 0 ft.!
' . ::3 .p r:q
. 0
p A 10 0
r::J
l!l A .[!l
e:l
10
Fig. 4.5 Heat Transfer Coeft1c1ent vs. F4
1 Km ,6P F4 • 9.20 b- 0.0627 b AtAHv + 6.58,
see equation 4.6
..-1 ~ .p ~ Q)
a ori F-t Q)
P4
~ ..
';:)0
26
10
0
LEGEND
0: 0.5 f•1embrane
.&..: 1.0 I:Lembrane G
El: 2.0 Hembrane 0 Y: 4.0 Hembrane
0
'Y A y
0 [!I
m .-mA
I!J
10 20
u , Calottlated 'from F4:uati'OnB 4.2 and 4.6 c
Fig. 4. 6 EXperimental Heat Tr&YSS:f'er Coefficient vs.
Heat Transfer Coefficient Calculated from
Equationa 4.2 and 4.6
50
.. C)
::>
51
26 LEGEND
0: 0.5 llfembrane
A: 1.0 f'Iembrane 0 A
2.0 Membrane 0 ~: 4.0 Membrane
0
0 t!J .. ..
0 1!1
0
U0 , Calculated from Equations 4.) and 4.6
Fig. 4.7 Experimental Heat Transfer Coefficient vs.
Heat Transfer Coefficient Calculated from
Equations 4.J and 4.6
5? ·-
the same type of apparatus, by previous authors (20, 27).
T'anna ( 27) concluded that diffusional resistance is not
the rate controlling factor for nass transfer. But the data
and results obtained during this investigation appear to
confirm the fact that mass transfer through water-repellent
membranes is by diffusion. rhe temperature differences of
these experiments were considerably less than those of I'anna•s
experiments. As has been discussed before, high f::l. t night
cause internal condensation and decrease mass transfer rates.
Thus his results should not be expected to produce the sace
conclusions as this investigation.
Rao ( 20) has developed a correlation for 1/!Sn, that
provided the best fit for his data, as follol'lS:
1 K
m
AP _ 0 • 0126 ( At - 1 . 4) b + 0. 00134 ~ t 6 liv
+ o • 3 54 ( A t - 1 .L~ )
SH' = 0.2688 J..J
(4.7)
using the same parameters as given by the above equation,
the following equation was obtained by fitting the data of
this investigation, i.e.
1 - = o. 049 3 ( At - 1 • 4) b + o. oo 303 ~ ~ A liv
+ 0.136 ( ~ t - 1.4)
SE = 0.7477
( 4. 8)
a d 4 8 By comparing coefficients in n 1 t 1s sho1-rn in Fig. • •
equation 4. 7 and 4. 8, it shows that they l·rere significantly
diff'erent.
53
10
LEGEND
0 . 0.5 J.Tembrane . £ : 1.0 I1e:m.brane .
.0 G): r-l 2.0 Hembrane
' . ._f9 •= 4.0 I•Iembrane r'-l y • ~
..-1
C\1 . 8 .p G-t
• J..l 4 ..t:: .&\. ..
'""'IJ=l 3
2
0 1 2 3 4 5 6 8 7 9 10
F5
Fig. 4.8 Reciprocal of r~SS Transfer Coefficient vs. F ..
5
AP F5 = O. o49J{A t - 1.4 )b + 0. OOJOJ At Aily
+ 0.1J6(At -1.4), see equation 4.8
I
I
On the other hand, by using the same parameters as in
equation L~.2 to fit }1aors data, the folloHing equation is
obtained
l -
54
{ 4. 9)
S,.., == 0. 647 5 .J:!,
and 1 t is Shot<In in Fig. 4. 9. In his results, the values of
1/JSn were generally v;ri thin 20.% of the values predicted by
equation 4.9. Comparing equation 4.2 to equation 4.9, it shovTS
that the coefficients of all three terms are reasonably close
to each other in the tHo equations. 'rhis fact emphasizes
that diffusional resistance might be the rate controlling
factor for mass transfer. The differences between the equa
tions are Probably due to differences in membrane preparation.
E. r·Iiscellaneous:
Findley (4) predicted that, t'lith the elimination of non
condensable gases from the pores, it should be possible to
obtain mass transfer by flow and rates should be considerably
higher. Six runs have been made to eliminate air by steaming
or boiling the membrane in the apparatus prior to testing.
Four tests have resulted in membrane failure or leakage due
to Pressure sur.ges or internal condensation. 'fhe other tl'To
runs have indicated no appreciable change in evaporation
rates attained.
55
7 ·-. ,0 r-t
6 .......... . bO ~ . 5 ~ s:: ..-t
N 0® . 4 +> \-4 ({;) G .
f.-! 3 ~
"IJ 2
1
0 8
Fig. 4.9i~ Reciprocal of Mass Transfer Coefficient vs. F6
~f.
. Data of Ro ..... o (20)
56
Thus far lt has been indicated in this investigation
that the rate controlling factor for mass transfer throuc;h met'l-
brane is the diffusional resistance, Considering that the
lo1v-er the molecular "t-reight of non-condensable gas the higher
the diffusivity, serveral attempts (5 runs) have been made to
replace air by helium. The results of tests 'tV"ith heliurr: and
air ·v1ere inconclusive, probably because of membrane variation,
but indications were that the use of helium increased K values ill
obtained.
.,
57
V. CONCLUSIONS
'rhe follo~'J'ing conclusions have been drawn from the data
and results obtained during this work:
(1) Diffusion through a trapped stagnant gas appears to be
the rate controlling mechanism for mass transfer through the
membrane.
(2) Over-all heat transfer resistance based on heat con-
ducted through the membrane is a linear function of membrane
thickness, but follows a theoretical equation (equation 4.4)
only after addition of an empirical constant (equation 4.6).
(3} Experimental values for De, ke, and h calculated under 2 2
the conditions used were 0.62 ft. /hr., o.4o4 Btu./ft. hr.
°F/ft., and 460 Btu./ft. 2 hr. °F respectively.
5t
VI. HECCHI'·IEEDATIOlJS
·The follolling reconnendations are suggested for further
study in this field:
(1) Effects of membrane characteristics of particle size,
composition, and particularly density, on the coefficients,
JSn and U c should be evaluated.
(2) High values of temperature differences are a possible
source of trouble in future experiments because of the possbil
ity of internal condensation. Additional study of the effect
of high temperature difference is recommended, particularl~r
if in an apparently economical range.
(3) The effect of elimination of non-condensable gases from
the pores and replacement of non-condensable gases by low
molecular 1'feight gases should be further studied.
(4) The next step in the evaluation of this process should
be Pilot plant type experiments, 1-11 th the design of such a
Pilot plant based on the results of this investigation. Such
experiments should provide information on performance at high
temperatures and pressures and continuous flot'l conditions·
60
APPENDIX A
MATERIALS
Salt (Sodium Chloride): Reagent grade NaCl was used for
preparing 7.0% by weight salt solution for evaporation.
Distilled Water: Steam condensate from the condensate line
was used.
Silver Nitrate: Reagent grade silver nitrate solution was
used to test the condensate for the presence of Cl- ions.
Teflon Dispersion: E. I. Dupont•s Teflon JO-B dispersion
was used for making the membranes. It is an aqueous disper
Sion containing 59.0 to 61.0% solids. It has a density of
1.5 gm./cm.J, a PH of 10.0 and a viscosity of 15.0 centipoise
at room temperature.
Q.lass Fiber: owens-Corning "Fiberglas", Type AA, of size
1 micron in diameter was used for making the membranes.
~uminum Sulfate: Reagent grade aluminum sulfate crystals
were used for preparing 0.05 gm./ml. solution.
~etic Acid: Glacial acetic acid of reagent grade was used.
APPENDIX B
I1EMBB.AJ.'JE CHARACTERISTICS
AND
DATA FOR HEAT LOSS APPROXIMATION
61
This appendix includes the characteristics of the mem
branes used during the investigation, and the experimental
data used for heat loss approximation of the apparatus.
Run No.
1
2
3
4
5 6
7
8
Note:
1.
2.
3.
4.
5.
6.
7.
8.
9.
62
'rABLE 13.1
Nembrane Characteristics
b Heasured gm. glass ~vt. per 'rhick- Wt. per fiber per unit area ness Density 0.115 ft.2 gm./cm.2
unit ar~a in. gm./cm.J lb./ft.
0.50 .0076 .020 .150 .0277
0.50 • 0105 .026 .159 .OJ84
1.0 .0139 .033 .166 . 0508
1.0 .01.36 .038 .124 .0497
2.0 .0280 .062 .178 .102
2.0 .0286 .069 .163 .104
4.0 .0511 .082 .246 .187
4.0 .0457 .101 .156 .167
Data on these membranes were measured after the transfer experiments.
Transfer area in experiments was 0.0246 ft. 2
~a4ao of Teflon to glass fiber in the membranes 1s • gm./gm.
~.
Density and thermal conductivity of Teflon are 2.20 gm./c~.J and 0.11 Btu./ft.2 hr. oF/ft. (8), respectively.
Volume fraction of glass fiber and Teflon are 0.0603 and 0.0.314, respectively. 3 Average density of all the membranes compressed = 0.226 gm./cm.
Average thickness of all the membranes compressed=0.00188b ft.
Average void fraction of all the membranes compressed= 0.91
Average uncompressed membrane densitY= 0.168 gm./cm. 3
(not used in calculations)
63
TABLE B.2
Data f'or Heat Loss Approximation of Apparatus
'Temp. of Temp. of
Power Salt Fresh Room
Input tvater Water Temp.
P, watts tcs• oc 0 tcf• C tor' oc
2.00 37.2 26.9 21.0
4.00 60.6 38.9 22.0
4.00 61.6 41.7 22.2
4.00 62.7 43.9 22.5
4.00 65.2 47.1 20.5
4.00 67.4 50.5 22.0
4.00 69.2 54.6 22.0
5.90 77.0 46.8 21.5
6.00 81.6 55.1 23.0
6.00 91.2 67.8 23.5
6.00 95.2 73.8 22.0
64
APPENDIX C
DATA AND RESULTS
The experimental data taken during the investigation and
the results obtained are included in this appendix. The vapor
pressure of 1·1ater at the salt and fresh water temperatures
are obtained from the equation {11)
log10 Pc _ x (a' + btx + ctx3) P - T' 1 + dtx
where p _ vapor pressure in atm.
Pc - 218.167 atm.
T - t°C + 273.16
X - Tc - T
Tc - 647.27
a• = 3.2437814
bt - 5.86826 x 1o-3
ct - 1.1702379 X 10-8
Cl - 2.1878462 X 1o-J
TABLE C .1
Run Number 1 (b = 0.50)
Temp. of Temp. of V.P. of V.P. of Amt. of Power Salt Fresh Salt Fresh Conden-Input Water water Water Water sate PT,watts ts, oF tr, oF Ps,in.Hg. Pr,1n.Hg. w, ml.
Mass Trans. Coeff .
Time Km , Dura- lb./hr. tion sq.ft. 9, sec. in. Hg .
Heat Trans . Coeff. Uc, Btu./hr. sq.ft. OF
0'\ \.1\
TABLE C.2
Run Number 2 (b = 0.50)
Temp. of Temp. of V.P. of V.P. of Amt. of Time Salt Fresh Conden- Dura-
Heat Trans. Coeff. Uc, Btuy'hr.
~ ~
TABLE C.]
Run Number J (b = 1.0)
Hass Heat Trans. Trans. Coeff. Coeff.
Temp. of Temp. of V.P. of V.P.of Amt. of 'l'ime ~:/hr. u%, Power Salt Fresh Salt Fresh Conden- Dura- B u./hr. Input Water Water WAter Water sate tion sq.ft. sq. ft. PT,watts ts, oF tr, oF p8 ,in.Hg. Pr,1n.Hg. W,ml. <9, sec. in.Hg. Op
•. ,,.J •~7\.lfe \_}._:;,:~
4.40 5602. 0.31 7.95 5363. 0.3Q
I i . ..., 'J ~ ~ ....... ' • • •• - • L '.- • - •• ~- 4. 15 3 1 71. 0. 29 oo tse; 7".\ 146.10 B. ~o 1. 31 1. rr---·117o. o. 3?.
tn:~o 14.\0
.. l4t.?Q • .,Q.~<1
146.51 ~.75 1.?1 2.50 1685. 0.32 1~0.~2 1?.30 10.27 2.40 1181. 0.32 161.1~ 1?.54 lQ_~48 2.45 1198. 0.32 161.18 Il.'>~ lO.zt~ .?.30 ll7R. 0.31 l5Q.~7 12.0Q 10.08 7.15 3556. 0.32 --177.~1 17.70 15.30 h.QO 2813. 0.33 17~.64 17.A~ 15.77 3.?0 1324. ~or.~3~Rr----------
-r7A.64 17.~0 1~.77 1.10 121A. 0.40 17~.64 17.AO 15.77 13.?0 5355. 0.3q
Q4.93 ?.5~ l.6R 1.?0 1~46. 0.?4 ~~-~? ?.5R 1.70 1.20 170?. 0.26
.~-~ ···~"' lefl t.uu tlbO. u. __ . Q~.40 ?.5R 1.70 3.4~ 470R. O.?h 1~1.1n ~.69 2.17 5.00 3000. 0.35 1~4.~? ~.Rl ?.26 ?.30 1340. 0.36
--T'1 c; • 'c; ---- ". ~ c; '. lt T."7'f---nrmr. o. ~7 lO~.oA ~.70 7.72 10.~0 614R. 0.1~ 110.01 ~.17 1.S~ 1.05 Q}O. 0.7A llO.~? ~.n~ ~.,7 6.7, 3lAO. 0.26 , '11 • 4 1 A. l '7 1 • 6 0 ___,-~- V) 4 () lt'l).. n ~------t?o.o~ ~.to ~.57 13.,0 q71,. O.?O 1~~.~0 ~.6? ~.7~ 7.~5 4q43. 0.13
0\ --.,J
Power Input T,watts
. ·-.oo .oo .0()
Temp. of Salt Water
0 t 8 , F
Temp. of Fresh \'later
0 tr, F
TABLE C.4
Run Number 4 (b = 1.0)
V.P. of Salt Water p8 ,1n.Hg.
V.P.of Fresh Water pr,1n.Hg.
Amt. of Condensate W,ml.
Time Duration e,sec.
Nass Trans. Coeff. k'm, lb./hr. sq.ft. in.Hg.
Heat Trans. Coeff. Uc, Btu./hr. sq.ft. OF
~~~- 0.4~ 26.26 1130. o. 37 ?q~--··---·---
l2qo. o.42 ?1.37 ?340. 0.32 13.40 1829. 0.34 11.04 ,.,, 0~ Il.OA
0.33 11.50 0.32 15.92 0.32 12.57
eJU J."TJ.eC-. c>e7P Ue.JU :Je ... U t:..l:;)l.e o.-31---~~~--rr
15~.71 t4o.6n s.qo 6.26 12.17 48?8. 0.32 12.92 17?.66 1~4.97 13.~0 9.00 6.17 149?. 0.32 13.P? 174.94 1~7.7? 1~.~? 0 .~2 4.~0 1078. 0.31 12.40
-------rrfl.~6 I'iR.4I 14.~7 q.9o -r.n·---- 899. o.3o -rr~-- .. 177.\? 1~Q.54 14.~~ 10.07 3.70 898. 0.29 12.07 11e.11 160.6~ 14.96 10.~~ 3.6o A65. o.?9 11.91 tR0.12 160.61 19.1? l?.Rl ~.tn ~96. 0.?7 10.65
---~- 3. l 0 I) 7 4. 0. 27 6. 74 1.10 ~98. 0.?6 10.46 ?.61 492. 0.26 6.55
187.04 167.17 lR.6~ 1?.09 5.60 10?0. 0.27 5.54 ~--TW"r."" t "1.11 '"· &4 tz. ne 11.11 -~----~~o7.- -rr.--zr ~. ?6
()'\
co
TABLE C.5
Run Number 5 (b = 2.0)
Nass Heat ;rrans. .rrans. Coeff. Coeff.
Temp. of Temp. of V.P. of V.P. of Amt. of ·rime I<m, Uc, Po'tier Salt Fresh Salt Fresh Conden- Dura- lb./hr. Btu./hr. Input \•Tater \'later Water Water sate tion sq.ft. sq.ft. PT,watts 0 tr,oF p8 ,in.Hg. pf,in.Hg. W,ml. e,sec. in.Hg. oF t 8 , F
~-~1ft ttf>.~~ ~.~.. ~-''- '·" ,_,., ''~· ~-~' 12.44 ~.oo tth.A1 q;.1o 3.12 r.12 t.eo rs21. o.z3 to.r9 --~.oo 117.0~ a~.52 3.14 1.72 2.20 2227. 0.2? 10.32 5.00 117.07 95.64 1.14 1.72 6.10 6378. 0.22 11.05 ~.on l2R.5t ltt.an 4.33 2.Rl 2.47 ?421. 0.22 10.15 r;. no 129.42 1 1?. 5" 4. 44 z. 87 2. 6rr-------- -z4o7. -- -----u-; zz ---~-;n-~.oo t3o.~q 11~A11 4.56 2.03 2.so 22eo. 0.22 7.5' 5.00 1?9.07 112.25 4.40 2.84 7.57 7103. 0.22 8.6R o.oo 16?.40 14~.06 10.36 7.19 3.57 1466. 0.?5 12.11 [U.OO 161.611 ___ 147.03 lO.nP 7.37 5.t:;o 71R4. 0.25 <?.R6 0.00 165.17 147.60 11.07 7.48 4.50 lPOl. 0.?2 9.50 o.oo 163.69 146.73 10.~9 7.32 13.57 5451. 0.24 10.19 0.00 165.62 14R.0'1 11.19 7.57 1.47 ______ 1297. 0.24 5.74
, ......... ,..,.0-=. -mJ-------Tbl)~ ''+R .1 q 11. 2' 1 .l)q .,-~1n ·· · · m-s~--- o. ?4 ~~-o?l_ .. c.on 165.~~ 14A.~l ll.'A 7.6? 9.57 ~57Q. o.24 5.65 ~.00 1PS.15 167.~6 17.60 1?.?4 3.Q7 945. 0.25 q.02 ~.06 1P7.40 1AQ. 0 5 lq.41 l?.Ql 10.60 753?. 0.?5 R.7~ 5.no tot.ot 17":\.?o 10.(}7 11.96 PJ.<:J4 46oo. o.?? a.cm -'s.06 lR5.~? lA7.7~ 17.A6 lO.R~ 5.67 l~ll. O.?l 5.9? s.oa l?~.3q l~l.P? ln.~4 tO.A4 ?.no 6oo. o.?3 6.4~
... _~1l.~.!L_ _______ 1~4.-11_ _!_~ _ _!_,_~ _____ _!_!_.!_11__ _____ to. 8~ _____ ~_f!_?J 1911· 9!22__ __ _ __ 6. 3(, ______ _
0'\ \.()
Pol'ler Input PT,watts
TABLE c.6
Run Number 6 {b = 2.0)
Nass Heat 'l'rans. rrans. Coeff. Coeff.
Temp. of Temp. of V.P. of V.P. of Amt. of 'rime Km, Uc, Salt Fresh Salt Fresh Conden- Dura- lb./hr. Btu./hr. Water \-later water water sate tion sq.ft. sq.ft. ts,oF tr,oF p8 ,in.Hg. Pr,in.Hg. W,ml. e,sec. in.Hg. Op
•·" '·• '·"' t.M ~.... o.~~ 12. ?1. A7.94 2.63 1.35 5.3o 625o. o.~ t:>."TT qp.R~ ?.70 1.39 1.00 1165. 0.21 11.97 ~7.00 7.60 1.31 9.60 112RO. 0.21 12.13
1~2.37 1~4.46 3.66 2.26 1.45 . 1703. 0.?0 13.49 1 2l. A1 1 !l5. 79 3. 70 2. 35 1.1)1) -d-- {()57. ~20 -rzt0T ___ _ 124.47 107.0R 3.~7 2.44 3.10 3442. 0.?0 1?.57 175.31 107.0~ 3.97 7.44 1.40 1562. 0.19 11.84 1?4.2R 106.?1 3.~6 2.3R 7.60 _R664. 0.10 12.61 156.14 136.9A A.99 5.67 1.40 61A. 0.?3 15.74 __ _ 1~9.~q 140.10 Q.63 ~.16 6.RO ?737. 0.23 10.Q5 16?.?5 141.16 10.37 6.~7 5.00 7009. 0.72 10.35 163.65 143.04 10.67 6.65 3.RO . 1570. 0.19 10.56
-- - r6-r. 31 ~-1 q 1 o. 33 6. 6 A 7T~1J?:r -- ----sTTu-.- -------o-~n- " - ... 1Rq.53 170.PQ 1R.A7 13.19 5.70 1466. 0.22 lAA.?l l70.A7 }R.73 13.19 5.00 1795. 0.2?
1') .. 'lO ~~
-...)
0
TABLE C.?
Run Number 7 (b = 4.0)
Nass Heat Trans. .rrans. Coeff. Coeff.
Temp. of Temp. of V.P. of V.P. of Amt. of rime y u Power Salt Fresh Salt Fresh Conden- Dura- l"¥5ihr. B%~./hr. Input Water Watgr Water vlater sate tion sq.ft. sq.ft. PT,watts ts,oF tf, F p8 ,1n.Hg, pf,1n.Hg. W,ml, e,sec. in.Hg. op
--!Ia lM!J~ "!~3 ~!~ '~~ t:ro t~n~ 8: ~~ l~6-- --~.00 123.0Q Q4.63 3.7? 1.66 ~.30 4322. 0.12 11.80 ~.00 125.37 Q7.50 3,Q6 1.81 2.10 ?760. 0.11 11.66 ~.oo 121.21 99.3~ 4.17 l.Q? t.Ro 2167. 0.12 10.56 -rs--;rrn--- I ?9. 4 5 103. q Q 4. 4c; 7. 2 3 -r.-gu-- ---·- .. "TJ1JT. ______ \J. 17 ·---~uu-··
5.00 131.2q 105.23 4.67 2.31 2.10 ?302. 0.12 8.01 ~.00 13?.82 106.47 4.R7 2.40 1.90 2064. 0.12 7.74
.00 131.16 105.?3 4.66 '· 31 5.QO _ ___!!758. 0.12 8.58 • J .L J " , • -:--; 7 ~ • ~- -· __ 1 .-~ • _ J .L - J • l.J '· 1 c_ !"~l .....,. t" • \1 • _,_ .J 1 t_J • ,J
161.32 139.30 Jn.on 6.03 5.60 3?00. 0.14 R.Ql 162.~6 l3Q.88 10.47 6.12 2.90 1647. 0.13 8.00 164.76 l3Q.73 10.Q6 6.10 1.50 811. 0.12 5.99 1AT.A4 1'39.BO 10.77 6.11 7~-l)·ry--·~ 1360. 0.1'3 ~u-· 16?.36 }3Q.31 10.35 6.03 17.50 7018. 0.13 7.77 lRt.qn l61.?A 16,?9 t0.4Q s.no 3660. o.l? 10.54
'. . . ., l p 1 • 7 6 l ~ 1 • p '+ 1 6. 2 4 1 0. 64 l • ~ () . ') q 2. 0. 1 3 1 0. 8 () ••.A ... >< ·lfP.nq 11)?.4~ 1A.v; 1o.An 2:-n11 qoq. 11.13 to.53 --·-181.~~ 160.10 16.16 10.10 11.10 484A. 0.13 7.82
~---------------------------------------------------------------------------------------~
-..,J ~
TABLE c.B
Run Number 8 (b = 4.0)
I·Iass Heat rrans. rrans. Coeff. Coeff.
'J~emp. of remp. of V.P. of V.P. of Amt. of ·rime Km. De, Power Salt Fresh Salt Fresh Conden- Dura- lb./hr. Btu./hr. Input Water Water Hater Water sate tion sq.ft. sq.ft. PT,watts ts,oF tr,oF p8 ,1n.Hg. Pr,in.Hg. W,ml. e,sec. in.Hg. OF
__ • \J, ., • L .L l. ov Jm! ~---- K! ~~ ----{!.;: A.?.8 6.21 1.40 1442. O.lS 5.11 A.43 6.30 2.0S 1983. 0.1~ 3.34
I __ ... J -~ ., _ • •• _ • _ _ _ _ 8 • o 1 6 • 16 6 • c; 2 . . . " q o 8 • _ o • t 6 _ . 6 • 2 n tn on pq q4 Jht l? 16 31 12 o7 z;f;rr---------r--o-c;-o·;--------u;-rr-------n;-crrt 4.~7 ?012. 0.19 B.O~ 5.60 2306. O.lq 7.49
I I"' • " .. ~ " ~ ... ., . - -· . ~ . ~ - . -- - ·- - --- 1 3 • o 1 c; 314 • o • 1 Q 1. ,;; 1 ___ _ 2.9o 198.13 1A3.R5 73.1° 17.72 4.31 1301. 0.20 A.oA ,.qn 199.73 lA4.76 ?3.9Q 18.09 10.10 3213. 0.18 7.65
i·~ ~g~:~' l":ti i~:~ li:41 1::'~ i~ii: &:l~ Z:6~ .I • ------- ... -·-· -------------- .. ·------------ -----------
-..,) l\)
l.
Power Input IP ...
5.~~
't=gg -.oo l .oo .()')
-·t!~ci l.oo ' .l') .80
.O'l t.lf)
't:~~ ,-.on ,,.0()
; • 00 18.00
'J.O'l 'J.()f) ,,.nn l . ()()
• 1)0 1 .no
'S.OI1 ').l')f)
10.0') tit. f)() "·nn -;.f)n A.O'l
10.11() ~.()()
1 n. oo t1.f!:tf'l
Temp. of Salt Water
0 -
·tt~.~~ lCJl.l1 1~?.45 ll'5.5R l4Q. l 1 179.?6 ]OS.4S 130.5? ]')').73 lA8.99 l8').Qf) 110.4? l ?3.P.3 140.34 11~-"A l?l.1A 1'5C5.71 1 74.04 }Qf).}Q 1 1 7. 07 17().()7 lf-1.1-.Q }f.,').AA }P7.4() 1P4.11 11'1. 0 1 l-:>?.~7 1f..?.7c:; loq·c;" 1~'1.~7
l ~ l • 1'' 1 ""'·Q" 1"'1.7f, ,,,.,_,7 \A"l.l-.7 ,..,..,_?"'
TABLE C.9
Data Used for Least-squares Analysis
·remp. of Fresh Water
0 -. ~~-"· 1 ~6.(}6
}F-,7.0t; 104."3'~ lV-t.Rl l'1~.9R 1 7 6.'51 l??.O? l4n.7" l'59.S7 1 7 P.. 64
Q'5.lt0 1 114.c:;? llg.')? l0R.77 lf'l7. 0 ? 1 4(). A 0 1"7.?? 17().')F,
QC:::. ,..,,.
ll?.?c:; l'tA. 71 }4A.1} l f")r).Q')
lA-:>.c:;t+ Q 7. Q '•
1 ")1, • '• /-., 1 '• ~ • l ,, 1 70.01"1
n7. r;'")
1 0 r • ., .\
1 -:\'"' • on l!,l.r>l, 1 '• n • 1 ,, 1 A~"' • 1 1 1 ... , •• ...,,,
V.P. of Salt Water
'· fW) 7.97 16.'11
3.01 7.49
l5.1Q ?l.QS
4.SR 8.9?
1?.11 17.~7
?.')Q
3. 'H r::;. Q7 1.?() 1.r::;r, q.q;:>
11.04 l<"~.A()
1.1c::: 4. '• l
1 0. 71 l 1 • ., q 1A.4S 17.1'1
? • ,._ ~ ~.~A
1".~'· 1 0 ')" . .
~ '17 . .
'•. ,, 7 1f".'•r:l 1 ".
.,., 0 ,..., .
lf-."" .,,_,,
V.P. of Fresh Water
-
'·" 5.68 17..09
?.;:>5 ').17
11.23 15.0'> 1.77 7. :p
10.10 1'>.80
1.71 ?.?6 3.'5? ?.')7 ?.'51 A.?1 c.c;4
13. l., l. 71 ?.AS 7.33 7.A3
l?.C4 l o. qc:;
1 • 1 c; ?.?f.. f...,, q
11. ?? 1 • q., ., • :q A.l 1t
lf).".t.. , • 1 q ,.,_"..,
t·~. 1?
Amt. of Condensate W.ml
4.6tt 3.40 q.oo 1.70 6.40 ?.?7 7.00 4.4'1 l. 75 7.1'5 3.20 3.40 2.30 6.?'5 1.?0 R.77
1 2. 17 4."() 1.10 ,.,.tn 7.~7
11."7 q.c;7
Jr'l. f. I) q. :::'7 c;.-:\f) 1.4'5 c:;.n, r::;.7"1 .,.11') c:;.of) 7.Q1 l.:l'1 ~."'.,
1 ~.rn ''l.7fl
·rime Duration e
4~1 • 1183. 2123. 1895. ?B47.
') 8 2. 1???. 5602. 1170. 1'556. 13?4. 470~. 1340. 3160. 1200. ~HQO. 4~2R. 107R.
J:;74. 617A. 7101. 5451. )r::;79. ?53? • 1911. ~::>c:;n.
1 7n~. -:>()nQ.
14t..~. ?71-.,0. A 7c:; q • l'A7.
t;;<1?. r, '1 n n • ~ ~ 71 •• ~,,,_
Nass ·:rrans. Coeff. Km, lb./hr. sq.ft. in.H
O.ltl 0.36 0.31 0.18 0.34 0.30 0.?7 0.31 0.3? 0.32 0.38 0.?6 0.1() 0.?6 0.42 0.11 0.~? 0.31 0.?7 0.22 0.22 0.24 o. ?4 0.?4 0.22 o. ?l 0.?0 0.?? O.?? (). t 1 n.12 0.13 0.13 f). 1 ~ f).lQ O.l•
Heat ·rrans. Coeff. Uc, Btu./hr. sq.ft. Op
lf..A.3 16.94
Q.Qt) ? 1. <ll ?1.77. P).06 13.tJR --------------
?1.37 11.'50 12;.Q2 12.40
f-..74 ll.O«:; 8.6~
10.39 5.61:; A.76 6.36
1?. 31 13.40 tn.3c; 7.4?
1 1 • ,.,_,., P.s:;q A.OO
1 0. PO A.?f.,
7. "l 7.6"
b
,., • '50' o.so 0.'50 o.c;o 0.50 0.50 0.50 I.on I.oo 1.00 1.00 1.00 1.00 l.OD 1.00 1.00 1.00 1.0(} 1.on ?.00 2.00 2.00 ?.00 2.00 ?.00 ?.00 ?.00 ?.on 7.00 1t .oo 4.00 4.on 4.()0 4.00 4.'ll') 4.no
""" \....)
74
APPENDIX D
COI.fPUTER PROGRAM
The program used for the computations described in this
thesis is given in this appendix. The program was written in
Fortran IV language and was run in IBI1 360 system.
/JGB /FTC
GO LIST
Cl YEH
C C***l7748L~X041 Y~H, C. L. S.0001 ~~1Tt(3,100)
S.0002 ~~l1t(3 1 20C) S.0003 A=3.2438 S.0004 B=~.B683E-3
S.COC5 C=l.l702E-S S.OOC6 0=2.1878t-3
·-- •. ---··•- - ' • •• T --- ·--- -- ----·-- --•-••• o •••--••-•••- ·--···•·-•- -~· •''
S.GGG7 AR=0.0246
ll/l~/66 RACS
S.G008 lC RtADtl,300)E~S,EMF,TCR,Xl,R,TlME,PGW S.OCC9 EMS=E~S+TCR/24.49
S.COlO E~f=EMf~TCR/24.49
S.OOll l~ttMS-2.45C)2G,20,30
S.0012 20 TCS=EMS*24.49 "'"··-~--·--·"-. - ~ ··- -~·------ -·-------------------~---- - .. ·----~-~-----------
S.C013 GC 10 40 S.0014 3G TCS=60.0+tE~S-2.450)*21.74 S.0015 40 lf(EMf-2.4~0)50,5~,60 S.0016 ~G TCF=EMF*24.49 S.0017 GG TC 70 S.OOl8 oC TCF=60.0+(E~F-2.450)*2l.74 '5~.0019 70 TFS='( r'cs~·i~*«Tcs=·ffRTltloo.-::rcR-) )*1.8+32.0 S.OOLU lff=(TCF-2.*<TCF-TCR)/(100.-TCR))*l•8+32.0 S.0021 OT=TFS-Tff S.0022 Hl=ll2c.l+C.396*(TFS-150.) S.0023 h2=1.8*TCR ~. oo24 .,.~=J~~.Li1-.!,~~-~--·· S.OC25 wH=w*3600./(454.*TIME*AR) S.0026 Ql=PG~*3.4128/AR s.oc~7 QV=~r*<Hl-H2> S.OOlB OQ=~T-QV S.0029 HTC=LQ/DT
OO'J2
oo3o ·-·----·- ,~~31~ .11- res -------------------=====-=-============== ..... ==~·-=,~·=·---··---
I oo 1 o 1
-..:> '-"
S.0031 AS=2.303*X/CTCS+273.16J*CA+B*X+C*X**3J/Cl.+O*X) 5.0032 Y=374.ll-TCF 5.0033 AF=2.103*Y/CTCf+273.16)*(A+d*Y+C*Y**J)/(l.+O*Y) S.0034 P~=b~2B.?*tXP(-AS) S.003? PF=t;28.5*~XP(-A~)
~.0036 Pt=PS*O.Y6 S.0037 CP=~f-PF S.00~8 ~TC=~H/DP S.003~ ~RITE(3,400)TFS,TFF,OT,OP,WH,HTC,~TC S.C040 IF(Xl-l.)lC,80,80 S.004l 80 STuP S.0042 luO FORMAT(lbl) s. 0043 200 fOt:tMA t ( 5-i;3-t:iTFS-,-:rx-;3-HT-FF ;ax-, 2H0i ~-ax, 2HOP, 9X, l HW, 8X, 3HHTC, 7 X, 3HWTC)
S.0044 300 FORMAT(7fl0.4) S.0045 400 fORMAT(4fl0.2,fl0.4,fl0.2,fl0.5) S.0046 END
~NO LF.COMPlLATION MAIN /DATA
SIZE OF COMMON 00000 PROGRAM 01480 >
--J 0'-
APPENDIX E
LEA.ST-SQUARES APPROXIIvlATING TECHNIQUE
The type of equation used :for analyzing the data and
result is
n y - 5: BjXj
j=l
77
where {xj}, j = 1, 2, .3' ••••• , n are a sequence of parameters
computed from independent variables, Bj 's are least-squares
constants, and Y is the dependent variable.
The program used for the computation of least-squares
constants is given in thiS appendix. It was prepared in
Fortr.an IV language, and was run on IBiv1 .360 system.
0014 0011) 0016 0017
• 0018
0=2.1878462E-3 AR=0.024
DO 13 1=1,7 GO TO t1,1,2,3,3,4,4l,l
GO TO S 2 T(J)=1.0
GO TO 5 3 T(J1=2 •
GO TO 5
GO TO 5 14 T ( J ) = T ( J- 1 )
)
--
5 READt1,300lEMS,EMF,TCR,Xl,W,TIME,POW -----------EMS=EMS+TCR/24.49 EMF=E~F +TCR/24.4
-..;] co
.0070
.0071
.0072
.0073
.0074
.0075
.0076
.0017
X(l,ll=AAAA Xft,Zl=BBBB X(l,3)=1. MJ=3
5'>5 CONTlNUE
I :aeV,I..,
s ..... S.Ol02
S.OlO S.Ol04 s.o1os S.Ol06 '5.0107
.0108 s.o1oq S.0110 s.o111 S.Oll2
.0113 S.Oll4
• 0115 • 0116 .0117 ---.Otl 8
'!I 21
c c
25
2
29 '30
XTFCIJ=SUM FINO INVERSEOF XTX : XI BY GAUSSIAN ELIMI NATION WlTH PIVOTING SET UP AUGMENTED MATRIX OF XTX. AND CHANGE THE NAME AS A
Jl=MJ+l MJ2=2*MJ DO 30 I=I.MJ DO 25 J=l.MJ A( I ,J}=XTXf {yJ)
DO 30 K=MJl,MJ2 I l=K-MJ lFtll-1129,28,29 ACI,Kl=l. GO TO 30 Atl,KI=O. CONTINUE SSSS=l • MARK=O • NMI=MJ-1 NN=2*MJ
__ 31
5,40,
CX> .....
Afl,l)=AfMAX,l) AfMAX,l )=TEMP IF ( NPLS V-l) 51
60 SSSS=-SSS 61 J= 62 J=J+l
' 51
lf(AtJ,I)l63,65,63 3 CON ST=-A ( J, I} I A (I ,.I)
l=I-1 64 L=l+l
A(J,Ll=A(J,Ll+A(I,Ll*CONS IF(l-NPLSYl64,65.64
65 IF(J-MJ)62.66.62 66 If(l-NMll32,67,32
II -:::: c COMPUTE DETERMlNANTtA) -67 TEMP= l.
1=0. 68 l=I+l
IF( AC I, t) )69,71,69 69 TEMP=TFMP*A(l,I) _-.:l:...:.F C l- MJ l 6 8 17 0, 6 8 70 DET=S<\SS*TEMP
GO TO 7 71 MARK= 1 1? IF(MARK-ll7~,9QQ,73 ~ I=MJ
81 l=l+l --- BACK SUt\STITUTJON
co 1\)
.0179
.0180
.0181
.018
.0183
.0184
.0185
.0186 .0187 .018 .0189 .0190 .0191 .0192 .0193 .0194 .0195
S.Ol96 s.o1Q7
5.019
c
86 87
88
89
F ( J)
+1
~0 ROR
r
co \..0
I • ... ·a aa rere·••L•..w•t~ ... ,..~.-• .:.-.n - ·- - ==-
C}l
92
qqq qq
100 101
''v
P(J)
co -{:::"
VIII. BIB-<=LIOGR.APHY
1. Bird, B. B. , Stewart, w. E-11Trans:port Phenoraena, n Jo~ • and Lightfoot, 1960, 'P• 520. \~iley and Sons,
. ' ~~. l .• ,
Inc., ;;c;; c ,. ,• '~ . . .
2. Ibid., p. 284.
3. Ibid., p. 245.
4. Findley, 11 • E. , uva.poriza t-;. :1 thr I & EC Pro c. Des and Dev ovn 1 o6ugh Foro6u.s Ecmbra.ncs ', _.-_.,;;;..;._..;:;...;;._.;;...:-..=...;;;..=::...::•~=-=:.::.....::::.;:.:...:.. • , o • , p • 2 2 · , 1 .. pr 11 , 1 ~: u 7 .
5. Foust_, A. S •, et a]..' "Pr::i_nciples of Unit cperation::; " John Wiley and Sons, Inc.. New Yorl{, 1959. p. 2. '
6. Ibid., p. 20.
Goodgame, '.I'. H. , Sherwood. 3: 37 ( 19 54- ) •
T. K., Cheo. Enc-:-;;. Sc.,
8. Hood, R. H .• , "Designing H~at Exchanger in l'cflo~1," Chem. b"'ne;r., Vol. 74, No. j_1, p. 101, !•:ay 22, 1~!~7.
9. Jhawar, H. N. , nSpecial Pr-oject on Nembranc::;," tnptfbl ~; :·.r :• Report tot'J'a.rds Bachelor's J)egree in Chen. Engr., t'n1v· :--sity of Nissouri at Rol~a • Rolla, Hissouri, 1967.
10. Keenan, J. H., Keyes, F. Giir • , "Thermodynanic Fropert!r:!": of Steam, n 1st ed. , John 1f..Jir :1ley and Sons, !Jew York, 191t7,
11.
12.
13.
14.
15.
16.
17.
18.
p. 28-33.
Ibid., p. 14. ti ~ ,.e .f' ro.,..e-- " 1~ .. ("lrl '";-··~~'>''
Kennard, E. H., nKine c ..L- .u ory o ... ~~ ·..:., ~ '-" ......... :, , ... -
Hill Book co. , NeW York, 1- 938, P. 65-69 ·
Lews \•I T(' ·wh1 trr»an, W • ' • .L-. ' d "r'\ ("*fl ...... c~ ......... •/ .. ~?~t , ...... ~ .. c:;- • ' In • ~:r..g • ...,. • ...... • ... · . .; .... '· ... ./ I .. •.. . .•
Lll sport J:= :roperties," Chc::o. Er'e::. :;ar.dbc c ..
4they,. P • E • • "T3ra.nH Eci:i- tor I·icGral.;-'H1ll ?:,cor: ,:;c ·' ed. ,. PerrY, • • ' '
New York, 1963, P• J-211 • J C::: nuni t cpero.t1ons c'!' C}:c::i r. ... al McCabe, W. L., Smi. th, •., ~;.,ol{ c ·· · ···o_,..·- "r·,'l ~ ,.. .. " Englneeri ng' " J.!cGra>~-EiJ.-'- .uv o • ' . • c" " •. ·. • • ~ ' • ,. . . : .
Ib·d ~ •• p. 611.
Ibid. • p. 928. 9-:l- ys l.s n Chem. Mr. !~and boo~:. Monet, G. p,, "EJ.ectrod~L tor,'J-:cGraw-01- ::;ook Co ..
4th ed., perrY• J • 11 • ~~ New York,. 196.3, P• 17 ~·
19.
20.
21.
22.
23.
24.
25.
26.
27.
28.
29.
Office of Saline Water, Dept. of Interior, nSaline w t Conversion Report for 1965," Supt. of Documents u '; er Govt. Printing Office, \iashington, D. c. • ' · ·
Rao, y. B. I 11 Study of Nass Trans:fer through Porous viater repellent Nembrane as a Function of Ivlembrane Thickness -and Rates of Heating," Unpublished Master's Thesis Libra University of tvlissouri at Rolla, Rolla, Hissouri, 196?. ry'
Rickles, R.N., and Friedlander, H. Z., "The Basics of Nembrane Permeation," Chern. Engr., Vol. 73, No. 9, p. 163 April, 1966. '
Sherwood, T. Extraction," 1952, p. 1 •
Ibid., p. 91.
Ibid. I p. 10.
Ibid., p. 10.
K., 2nd
and Pigford, R. L. 1 "AbSorption and ed., McGraw-Hill Book Co. , New York,
Tanford, c., nphysical Chemistry of Macromolecules," John Wiley and Sons, Inc., New York, 1961, p. 346.
Tanna, V. V. , nStudy of !>lass Transfer through Porous Water-repellent Jl1embrane," Unpublished 1•1aster' s 'rhesis, Library, T1957, University of Missouri at Rolla, Rolla, I-11ssouri, 1966.
Tuwiner, s. B., "Diffusion and Membrane Technology," Reinhold Publication Corp., New York, 1963, p. J.
Ibid. , p. 1.
IX. ACKNOvlLEDGEr·:ENT
The author wis.hes to express his sincere app :recia tion to
his research advisor, Dl::'. H. E. Findley, Associat € Professoi ..
in Chemical Engineering. for his guidance and sug ~est ions dur
ing this investigation. He also would like to ex:)Jress his
thanks to the Office of Saline Water, U. S. Dept. of Interior,
for the research assistanship.
·rhe author is also deeply indebted to his fa:t::nny for
their encouragement and continuous moral support.
X. VITA
r.rhe author HaS born 011 September 2.3' 19.39' in Tokyo'
Japan. He attended high school in I-lan, Taiwan, Rep. of
China, and graduated in June 1958. After high school, the
author entered Tunghai University, Taichung, Taiwan, Rep. of
China, in September 1958, and graduated in June 1962 with the
degree of B. s. in Chemical Engineering. He served in the
Rep. of China Army one year and was employed by Mobil-China
Allied Chemicals Corp. from September 196.3 to August 1965.
The author enrolled in the Graduate School of University
of Hissour1 at Rolla in January 1966.