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CHAPTER 4
MATHEMATICAL MODELLING
4.1 INTRODUCTION
A mathematical model usually describes a system by a set of
equations that establish relationships between the variables of the system. The
values of the variables can be practically anything. However the variables
which represent some properties of the system, has a definite range. The
actual model is the set of functions that describe the relations between the
different variables. A general approach to the mathematical modelling process
is as follows.
1. Identifying the problem and defining the terms in the problem
with diagrams.
2. Beginning with a simple model stating the assumptions.
3. Identifying the important variables and constants and
determining how they are related to each other.
4. Developing the equations that express the relationships
between the variables and constants relaxing the assumptions.
Once the model has been developed and applied to the problem, the
resulting model solution must be analysed and checked for accuracy. It may
require modifying the model for obtaining reasonable output. This refining
process should continue until obtaining a model that agrees as closely as
possible with the experimental observations.
51
4.2 IMPORTANT POINTS CONSIDERED IN MODELLING
The important points considered in the development of
mathematical model are
1. Model should be simple to build, simple to modify,
understand and to communicate its output.
2. Simulation should not necessarily be thought of as another
technique for finding optimal solutions to problems. However,
once a simulation model has been developed, a quantitative
analyst may vary certain key design parameters and observe
the effect on the output of the computer runs.
3. In ideal compressors, the suction and discharge take place at
constant pressure. Constant pressure suction or discharge is
possible only for the compressors with open head during
suction or discharge, or the compressor speed should be
maintained zero. But, both the conditions are impossible in
actual practice. The ideal compressor operation is not affected
by valve area or speed.
4. The polytropic index of compression and expansion is
constant and the value is less than adiabatic index for an ideal
compressor. But, in actual case, the polytropic index may have
any value depending on the direction of heat transfer. During
compression, it is assumed that the surrounding temperature is
less than the air temperature and heat transfer from the air to
the surrounding makes an index of compression less than
adiabatic index, for ideal case. In the actual case, at the earlier
stages of compression, the wall temperature will be greater
than the air temperature and the heat will be transferred from
52
the wall to the air. This will make the index of compression
more than adiabatic index. Once the air temperature reaches
the wall temperature, the index of compression will be equal
to adiabatic index, and thereafter the value will be less than
adiabatic index. The same is true for index of expansion.
5. The cylinder wall temperature will not be constant along the
length of the cylinder during compression and expansion. This
will vary the heat transfer pattern and index of compression or
expansion.
6. The volume just above the valve plate is called ‘Head
volume’. The air enters the cylinder from atmosphere to the
cylinder through the head. The air first enters the head and then
to the cylinder. During suction, there will be a sudden pressure
drop on the suction side head and this greatly affects the mass of
air drawn by the compressor. Similarly, the air from the cylinder
is discharged to the delivery head and then to the reservoir.
There will be a pressure rise in the head and the discharge will
be between the head pressure and the cylinder pressure and not
between the discharge pressure and the cylinder pressure.
7. Since the pressure during suction is not constant, the
volumetric efficiency cannot be determined from the
discharge pressure and clearance ratio as in the ideal
compressor. It should be determined from the mass of air
drawn or mass of air delivered by the compressor per cycle.
8. The indicated power should be calculated using integration
method from pressure and volume at different crankangles.
(Area enclosed by the curves in a p-V diagram is equal to the
net work transfer or net heat transfer as per first law of
thermodynamics).
53
9. Hitting of valve on valve stop by sudden opening, may make
the valve to vibrate. The valve will get stabilised only after
some degrees of crankangle rotation. This phenomenon may
reduce the mass of air discharged. This loss is dependent on
the velocity of valve with which it hits the stop.
10. The temperature of air entering the cylinder will not be at
atmospheric temperature. The air enters the cylinder from the
hot head chamber. There will be heating of the incoming air
and this will reduce the volumetric efficiency. In addition,
there will be an increase in indicated power due to increased
initial temperature of air during compression.
11. The discharge coefficient cannot be taken as constant during
discharge process or suction process. It varies with valve lift,
pressure ratio and the compressor speed.
12. Whenever the valve closes there will be a flow of some
discharged air back into the cylinder and this reduces the mass
discharged per cycle. Similarly during suction process, when the
valve closes some air would flow out of the cylinder. This will
reduce the mass drawn in per cycle. This phenomenon is called
back flow that results reducing the volumetric efficiency.
13. Blow-by losses are also considered while estimating the
volumetric efficiency.
4.3 FUNDAMENTAL EQUATIONS
The equations corresponding to the instantaneous energy balance of
the air compressor during suction, compression, re-expansion and discharge
are given below. The derivations are given in Appendix 1.
Figure 4.1 shows the p-V diagram of an ideal compressor cycle. All the
processes are assumed reversible.
54
d
p
ab
c
V
Figure 4.1 Pressure-Volume diagram of an ideal compressor
Figure 4.2 illustrates the control volume for suction and discharge
processes. At time t, the air in the control volume is at pressure p, volume V,
temperature T and mass m. After the time interval dt, the corresponding
values are, p+dp, V+dV, T+dT and m+dm.
For the processes shown in Figure 4.1, the instantaneous energy
balances or applying the first law of thermodynamics to these unsteady flow
and non-flow processes are
Suction(ab):
0dt
dQRTTC
dt
dm
dt
dV
V
mRT
dt
dTmC sv
sv (4.1)
Compression(bc) and Re-expansion(de):
0dt
dQ
dt
dV
V
mRT
dt
dTmC
v (4.2)
55
PistonPiston
t+dt t+dt
p+dp
V+dV
m+dm
T+dT
p+dp
V+dV
m+dm
T+dT
F F
dm - dm
p,V,T,m p,V,T,m
t t
Discharge(cd):
0dt
dQTCRT
dt
dm
dt
dV
V
mRT
dt
dTmC vd
dv (4.3)
4.2 a Suction process 4.2 b Discharge process
Figure 4.2 Control volume for suction and discharge processes
Governing equation for determining the instantaneous cylinder
pressure is
n
1i
ii )T(B1RT
pv (4.4)
The second term in equation (4.4) accounts for compressibility
factor and is negligible for single stage reciprocating air compressors.
Governing equation for determining the mass flow is
d
dm
d
dm
d
dm
d
dm opoi (4.5)
56
Q2
where, mop is the mass of air flowing through the gap between the piston and
the cylinder wall.
Governing equation for determining the working volume is
22
c
cc
sin)r/l(1
cossin)r/l(sin
2
LA
d
dV (4.6)
The volume of air trapped between the piston and cylinder head at
any crankangle can be determined using the properties of crank mechanism in
terms of the length of the crank lever r, the length of the connecting rod lc, the
stroke L and the cross-sectional area Ac.
The instantaneous heat transfer between the cylinder and air at any
crankangle ( ) consists of three quantities.
Q1 = Heat transfer between the air and the cylinder surface
Q2 = Heat transfer between the air and the piston surface
Q3 = Heat transfer between the air and the cylinder cover
Figure 4.3 shows the various elements of heat transfer in a
compressor.
Figure 4.3 Heat transfer in reciprocating compressor
Q1
Q3
57
The instantaneous heat transfer is estimated using
ccccppcscs ATTATTATT)(1
d
dQ (4.7)
where, ) is the heat transfer coefficient, Acs is the cylinder surface area, Ap
is the piston area and Acc is the cylinder cover area.
The heat transfer coefficient is obtained using,
Nu = C (Re)m (Pr)
n (4.8)
The constants C = 0.75, m = 0.6 and n = 0.8 are used in the
equation from the work of Ruihu Liu and Zicheng Zhou (1984). The
following data correlations are used to calculate the temperatures.
The temperature of the cylinder wall inoC,
Tcs = 24.32 + 0.7191 Ts + 5.64 (p /ps)
– 17.936 (x/D) + 14.183 (x/D)2
(4.9)
where, x = distance from the cylinder head to a certain point of wall in mm,
D = bore in mm, Ts = suction temperature inoC.
The temperature of the cylinder head in oC,
Tcc = 13.64 + 0.7191 Ts + 11.235 (p /ps) (4.10)
The temperature of the piston inoC,
Tp = 32.48 + 0.3 Ts + 9.243 (p /ps) (4.11)
58
4.4 INDEX OF COMPRESSION AND EXPANSION
The details of index of compression and expansion are summarised
as follows from the work of Werner Soedel and Rajendra singh (1984). The
compression and expansion of air in the reciprocating compressors may
follow any one of the following thermodynamic processes:
1. Isentropic 2. Adiabatic 3. Polytropic 4. Isothermal
The compression and expansion are said to be isentropic if
the cylinder is perfectly insulated, so that there is no heat
transfer between the air and atmosphere
there is no heat generation due to friction between the piston
and the cylinder wall
During isentropic compression and expansion, the entropy is
constant. n = 1.4 if the law of compression and expansion is pVn = C. The
compression and expansion are said to be adiabatic if the cylinder is perfectly
insulated so that there is no heat transfer between the air and atmosphere and
there is heat generation due to friction between the piston and the cylinder
wall.
During adiabatic compression and expansion, the entropy is
increased since the heat of friction is added to the air. n = 1.4 if the law of
compression is pVn = C
The compression and expansion are said to be polytropic if
the cylinder is not insulated and there is heat transfer between
the air and the atmosphere
59
there is heat generation due to friction between the piston and
cylinder wall
This type of compression and expansion is preferable in
reciprocating compressor cycle. The law of compression is pVn = C.
The compression and expansion are said to be isothermal if
the cylinder is a perfect heat conductor, so that the
temperature remains constant during compression and
expansion
This type of compression is ideal and requires minimum power for
compression. n = 1 if the law of compression and expansion is pVn = C.
4.4.1 Value of index of compression (nc)
Case (i) The cylinder wall temperature is assumed to be equal to the
ambient temperature
The temperature of air will be greater than the wall
temperature throughout the compression
The value of nc is always greater than 1 and less than 1.4
The heat is transferred from the air to the surroundings
through the cylinder wall
The value of nc depends on the rate of heat transfer between
the air and the surroundings (or depends on the thermal
conductivity of the material and the surface area)
60
Case (ii) The cylinder wall temperature is greater than the temperature
of air at the beginning of compression
In practice, the temperature of the cylinder wall will be higher
than the ambient temperature
During the earlier stages of compression the heat may be
transferred from hot cylinder to relatively cold air and thus
reversing the heat transfer making the value of index of
compression greater than 1.4
The index of compression becomes 1.4 when the air
temperature equals the wall temperature
The index will be less than 1.4 if the air temperature is greater
than the wall temperature and thus reversing the direction of
heat transfer
In general,
for heat flow from air to wall 1 < nc < 1.4
for heat flow from wall to air nc > 1.4
for no heat flow between wall and air nc = 1.4
(Temperature of wall = Temperature of air)
4.4.2 Value of index of expansion (ne)
Case (i) The cylinder wall temperature is assumed to be equal to the
ambient temperature
The temperature of air will be greater than the wall
temperature throughout the expansion
61
The value of ne is always greater than 1 and less than 1.4
The heat is transferred from air to the surroundings through
the cylinder wall
The value of ne depends on the rate of heat transfer between
the air and the surroundings (or depends on the thermal
conductivity of the material and surface area)
Case (ii) The cylinder wall temperature is less than the temperature of
cylinder air at the beginning of expansion
In practice the temperature of the cylinder wall will be
marginally higher than the ambient temperature but less than
the temperature of cylinder air (at high pressure) at the
beginning of expansion
During the later stages of expansion the temperature of the
wall may become equal to the temperature of the cylinder air
thus making the index of expansion equal to 1.4.
Usually there will not be a reversal of heat transfer during
expansion since the duration of expansion is less compared to
the compression
Reversed heat flow will make ne greater than 1.4
In general, for heat flow from air to wall 1<ne< 1.4, for heat flow
from wall to air ne > 1.4 and for no heat flow between wall and air ne = 1.4.
(Temperature of wall = Temperature of air)
62
3
p
41
2
VV2V4V3 V1
4.5 ANALYSIS OF AN IDEAL COMPRESSOR
Figure 4.4 shows the p-V diagram of a complete cycle of an ideal
compressor. All the processes are reversible.
Figure 4.4 p-V diagram of an ideal compressor cycle
Process 1-2 Polytropic compression with index of compression ‘n’
Process 2-3 Constant pressure discharge
Process 3-4 Polytropic re-expansion with index of expansion ‘n’
Process 4-1 Constant pressure suction
Compression of air in the cylinder follows the law pVn = C. Work
is done on the air during compression.
The work of compression is given by
1n
VpVpW 1122
21 (4.12)
63
The flow work during discharge is given by
)VV(pW 32232 (4.13)
The work of expansion is given by
1n
VpVpW 4433
43 (4.14)
The flow work during suction is given by
)VV(pW 41414 (4.15)
The indicated power (IP) is given by
= Wnet N/60 (4.16)
where, Wnet is the net work in the cycle.
60
N1
p
p)VV(p
1n
nIP
n/)1n(
1
2411 (4.17)
The volumetric efficiency ( v) is given by
31
41
n/1
1
2v
VV
VV
p
pkk1 (4.18)
where, k = Clearance ratio = V3/(V1 – V3) (4.19)
64
4.6 MODEL FORMULATION
The various models developed are shown in Table 4.1.
Table 4.1 Models developed
Model Nature of model
SP model Single-port model – Model of ideal compressor without
valves.
MP Static model Multi-port static model – developed for the compressor
with valves, but without valve dynamics.
MP Dynamic
model
Multi-port dynamic model – developed for the
compressor with valve dynamics.
4.6.1 Equations applicable to all the models
Figure 4.5 shows the schematic diagram of a reciprocating
compressor showing various forces acting on the moving parts and
component physical dimensions.
The cylinder area is given by Ac2D
4(4.20)
where, D is the bore in m.
The cylinder volume at any crankangle ( ) is calculated using
r
l2
sincos1rD
4VV
c
22
c (4.21)
where, Vc is the clearance volume in m3, D is the bore in m, r is the crank
radius in m, lc is the connecting rod length in m and is the crankangle in deg.
65
BDC
TDCFp
D
Vc
lc
Fcr
Figure 4.5 Schematic diagram of reciprocating compressor showing
physical dimensions
Cylinder volume is the sum of clearance volume and swept or
stroke volume. The first term Vc in equation (4.21) is constant at all the
crankangles. The second term indicates the instantaneous cylinder volume.
The cycle of operation is completed in 360o crank rotation. When the piston
moves from TDC (Top Dead Centre) towards BDC (Bottom Dead Centre),
the position of the TDC is assigned a crankangle of 0o and BDC is assigned a
value of 180o. When the piston moves from BDC towards TDC, the BDC is
assigned 180o and TDC is assigned 360
o. When = 0
o or 360
o the 2
nd term in
66
equation (4.21) becomes zero and the cylinder volume becomes the clearance
volume. When = 180o the 2
nd term becomes the stroke volume.
The velocity of piston (Vp) at any crankangle is estimated using
)2sin(l2
rsinrV
c
p (4.22)
The velocity of the piston is zero at = 0o, 180
o and 360
o where the
acceleration is also zero.
The acceleration of piston (ap) at any crankangle is calculated using
r/l
2coscosra
c
2
p (4.23)
Angular velocity,60
N(4.24)
where, N is the compressor speed in rpm.
The velocity of the piston is zero at 0o, 180
o and 360
o. The piston
accelerates from 0o to 90
o and 180
o to 270
o crank rotation and decelerates
from 90o to 180
o and 270
o to 360
o. The acceleration or deceleration of the
piston has a direct effect on the net force on the piston.
The resultant force on the piston (Fp) at any crankangle is
calculated using
preccase
2
p am)pp(D4
F (4.25)
67
where, p is the pressure at any crankangle in Pa, pcase is the crankcase
pressure in Pa and mrec is the mass of reciprocating parts in kg.
The resultant force on the crank (Fc) at any crankangle is calculated
using
22
c
pc
sin)r/l(2
2sinsinFF (4.26)
The resultant torque (Tr) at any crankangle is calculated using
rFT cr (4.27)
The area of port (Ao) is calculated using
2
oo d4
A (4.28)
where, do is the diameter of port in m
The density of air ( ) at any crankangle is calculated using
RT
p(4.29)
where, R is the gas constant in J/(kg.K)
The cylinder pressure (p ) at any crankangle during compression
and re-expansion is calculated using
n
11
V
Vpp (4.30)
68
where, = 0 corresponds to TDC, ( -1) denotes the previous crankangle
n = nc during compression process and n = ne during re-expansion
process
The temperature of air (Tc) at any crankangle during compression
and re-expansion is calculated using
1n
11
V
VTT (4.31)
The Free Air Delivered (FAD) by the compressor is calculated
using
a
aos
a
aod
p
RTm
p
RTm
FAD
1
4
3
2
(4.32)
where,3
2
odm is the total mass of air delivered to the reservoir in kg/s,
1
4
osm is the total mass of air inducted into the cylinder in kg/s, Ta is the
ambient temperature in K and pa is the atmospheric pressure in Pa.
The volumetric efficiency ( v) of the compressor based on mass is
calculated using
a
sa
od
v
RT
Vp
m3
2
(4.33)
69
Stroke volume, LD4
V 2
s (4.34)
4.6.2 Modelling of ideal compressor (SP Model)
An ideal compressor is the one which works on the thermodynamic
cycle consisting of all reversible processes.
The following are the assumptions made in modelling and analysis
of ideal compressor cycle:
1. All the processes are ideal.
2. Suction and discharge takes place at constant pressure.
3. Expansion and compression follows the law pVn = C.
4. Suction temperature is atmospheric.
5. Mass discharged or drawn per cycle is independent of port
size and speed.
6. No discharge loss or suction loss due to ‘back flow’.
7. No leakage loss (Blow-by loss).
8. Index of compression and expansion is same and constant
during a process.
9. No pressure drop in the suction line (between atmosphere and
compressor) and no pressure drop in the delivery line
(between reservoir and compressor).
10. Suction head air pressure is atmospheric and is constant
during suction.
11. Suction head air temperature is atmospheric and is constant
during suction.
70
12. Delivery head air pressure is equal to the discharge pressure
and is constant during discharge.
13. Delivery head air temperature is equal to the cylinder air
temperature during discharge.
14. No effect of heat transfer on index of compression and
expansion.
15. Coefficient of discharge is constant.
4.6.2.1 Suction and discharge
The pressure during suction and discharge is constant. The work
done on the air during discharge is utilised only for the removal of air from
the cylinder.
The mass of air inducted in or discharged out (mo) during is
calculated from
)VV(m 1o (4.35)
where, denotes the crankangle while -1 denotes the previous crankangle
The net mass in the cylinder during suction at any crankangle (mrs, )
is calculated from
os,1rs,rs, mmm (4.36)
The mass remaining in the cylinder during discharge at any
crankangle (mrd, ) is calculated from
od,1rd,rd, mmm (4.37)
71
The temperature of air at any crankangle (T ) is calculated from
11r,
11r,
Vpm
TmVpT (4.38)
The pressure at any crankangle (p ) is calculated from
r,
V
RTmp (4.39)
The total mass inducted in per cycle (mo) is
o,o mm (4.40)
Suction and discharge are flow processes and the indicated power
at any crankangle (IP ) is calculated using
60
NVpVpIPIP 111 (4.41)
4.6.2.2 Compression and expansion
Compression and expansion are non-flow processes and the
indicated power at any crankangle (IP ) is calculated using
60
N
1n
VpVpIPIP 11
1 (4.42)
n = nc during compression
n = ne during re-expansion
Though the equations (4.41) and (4.42) are similar, the values of p
and V are different for the non-flow and flow processes.
72
p -1
p
V -1 V
4.6.3 Development of MP static model from SP model
The suction and discharge valves are introduced in MP static
model. The model is developed with constant flow area without valve
dynamics. The maximum flow area both in suction and delivery sides is
considered. An effective model for determining the indicated power is
introduced in the model. The following assumptions have been eliminated
from the ideal compressor cycle analysis for modelling the reciprocating
compressor without valve dynamics:
1. All the processes are ideal
2. Constant pressure suction and discharge.
3. Mass discharged out or drawn in per cycle is independent of
port size and speed.
4.6.3.1 Estimation of indicated power
The area under the curve in a p-V diagram is work transfer or
indicated power transfer. Figure 4.6 shows the integration method of
determining the indicated power of the actual compressor cycle.
Figure 4.6 Integration method of determining IP
Since all the processes do not follow the particular thermodynamic
law, equations (4.41) and (4.42) cannot be used for estimating the IP. The
73
xs
general and effective model used for estimating IP during any incremental
crankangle is
60
N
2
pp)V(VIPIP 1
11 (4.43)
4.6.3.2 Suction process
The flow area is calculated assuming that the valve opens
immediately and occupies maximum effective lift. And the area is assumed to
be constant during suction. Figure 4.7 shows the plan and side views of
suction ports on the valve plate. The actual holes are shown by circles.
However for mathematical modelling the holes are assumed to be in-line as
shown by the dotted circles. Valve plate
Holes in plate
Plan view Side view
Figure 4.7 Suction port plan and side views
The maximum flow area considering only first mode of vibration isgiven by
Afs = dos Ssmax (4.44)
where, Ssmax = Maximum effective suction valve lift.
74
s
ss
maxsl
xhS (4.45)
where, xs is the distance between the centre of the port and base of the suction
valve in m.
The flow of air through the valve is considered as flow through a
nozzle. The mass of air entering the cylinder during is estimated using
ss n/)1n(
a
aa
s
sdsfsos
p
p1/p
1n
n2CAm (4.46)
where, a is the density of air at atmospheric pressure and temperature, ns is
the suction index and Cds is the suction side coefficient which is dependent on
the compressor speed and from the test results of the present work the
following empirical equation was developed for estimating Cds. The details
are given in Appendix 6.
)N00022.0N10x3N10x2.2(6.0C 28312
ds (4.47)
where, N is the speed in rpm.
The temperature of air in the cylinder at any crankangle is
calculated from
rs,
sos11rs,
m
TmTmT (4.48)
The mass of air remaining in the cylinder, the total mass of air and
the pressure of air are estimated from equations (4.36) to (4.40).
75
Stop
hSmax
l
Valve
X
Y
ValveValve
Stop
Valve PlateF
4.6.3.3 Discharge process
The discharge flow area is calculated assuming that the valve opens
immediately and occupies maximum lift. The area is assumed to be constant
during discharge. Figure 4.8 shows a reed valve in closed position and Figure
4.9 shows a reed valve in fully open position.
Figure 4.8 Reed Valve in closed position
Figure 4.9 Reed Valve in open position
The maximum flow area considering only first mode of vibration is
given by Afd = dod Sdmax (4.49)
where, Sdmax = Maximum valve lift ,d
dd
maxdl
xhS (4.50)
76
Mass of air leaving the cylinder during is estimated using
p
p1p
1n
2nCAm
dd 1)/n(n
d
d
dddfddod (4.51)
where, d is the density of air at discharge pressure and temperature, nd is the
discharge index and Cdd is the discharge side coefficient which is dependent
on the compressor speed and from the test results of the present work the
following empirical equation was developed for estimating Cdd. The details
are given in Appendix 6.
)N0002.0N10x3N10x2(65.0C 28312
dd (4.52)
where, N is the speed in rpm.
The temperature of air in the cylinder is calculated using
vrd,
2
p1pod1v1rd,
Cm
/2VTCmTCmT (4.53)
where, Vp is the velocity of piston in m/s and Cp and Cv are the specific heat at
constant pressure and constant volume respectively in J/(kg.K).
The mass remaining in the cylinder, the total mass of air and the
pressure of air are estimated using equations (4.37) to (4.40).
4.6.4 Development of MP dynamic model from MP static model
MP dynamic model is developed with valve dynamics considering
various losses and head volume. The only assumption in the MP dynamic
model is ‘expansion and compression follows the law pVn = C’. The suction
and delivery valve lifts at different crankangles are considered in the flow
77
area apart from other equations used in MP static model. The various
assumptions are relaxed in stages to study their effects on model performance.
4.6.4.1 Stage 1
In Stage 1, a simple valve dynamics concept is used to study the
behaviour of the valves. The assumptions eliminated from MP static model
are as follows.
1. No pressure drop in the suction line (between atmosphere and
compressor)
2. No pressure drop in the delivery line (between reservoir and
compressor)
The net force on the suction valve (Fs) is calculated using
soshss ZAppF (4.54)
where, phs is the pressure of air in the suction head in Pa, Aos is the suction
port area in m2 and Zs is the number of suction ports.
The initial force on the suction valve (Fsi) is calculated using
soseshssi ZAppF (4.55)
where, pes is the effective suction pressure in Pa.
The natural frequency of suction valve ( ns1) in I-mode is estimated
using
3
ss
s1ns
lm
EI55.3 (4.56)
78
where, ms is the mass of suction valve in kg and Is is the area moment of
inertia of suction valve in m4.
The suction valve stiffness (ks) is estimated using
2
nsss mk (4.57)
Using simple valve dynamics, the suction valve lift is calculated
from
s
siss
k
FFS (4.58)
The suction flow area in the I-mode is estimated using
2
)YS(dA ss
os1fs (4.59)
where,s
ossss
x
2/dxSY (4.60)
The natural frequency of suction valve in II-mode as stated by
Francis (1965) is obtained using 3
ss
s2ns
lm
EI22 (4.61)
Suction valve stiffness and lift are calculated from Equation (4.57)
and Equation (4.58).
The suction flow area in II-mode is calculated from
Afs2 = dos (Ssmax + Ss in second mode) (4.62)
79
where, Ssmax = Maximum suction valve lift and is calculated using equation
(4.45).
The net force on the discharge valve (Fd) is calculated using
dodhdd ZAppF (4.63)
where, phd is the pressure of air in the delivery head in Pa, Aod is the area of
the discharge port in m2 and Zd is the number of discharge ports.
The initial force on the discharge valve (Fdi) is calculated using
dodhdeddi ZAppF (4.64)
where, ped is the effective discharge pressure in Pa.
The movement of the valve till it hits the valve stop is considered as
the vibration in I-mode and the movement of the valve beyond the stop is
considered as the vibration in II-mode.
Note: The II-mode of vibration in suction reed and I-mode in delivery
reed are shown in Figure 3.3.
The natural frequency of discharge valve ( nd1) in I-mode as stated
by Francis (1965) is estimated using 3
dd
d1nd
lm
EI55.3 (4.65)
where, E is the young’s modulus of valve material in N/m2, md is the mass of
discharge valve in kg and Id is the area moment of inertia of discharge valve
in m4.
80
The discharge valve stiffness (kd) is estimated using
2
nddd mk (4.66)
Using simple valve dynamics the discharge valve lift (Sd) is
estimated from
d
didd
k
FFS (4.67)
The discharge flow area in the I-mode is obtained using Figure 4.9
as
2
)YS(dA dd
od1fd (4.68)
where,d
odd
ddx
2/dxSY (4.69)
The natural frequency of discharge valve in II-mode ( nd2) as stated
by Francis (1965) is obtained from
3
dd
d2nd
lm
EI22 (4.70)
Discharge valve stiffness and lift in II-mode are calculated using
Equation (4.66) and Equation (4.67).
The discharge flow area in II-mode is estimated from
Afd2 = dod (Sdmax + Sd in second mode) (4.71)
81
where, Sdmax = Maximum valve lift and is calculated using
equation (4.50)
4.6.4.2 Stage 2
In Stage 2, the effective valve dynamics and improved flow model
are used. Backflow in suction and delivery sides is considered.
Using improved valve dynamics the suction valve lift as stated by
Piechna (1984) is estimated from
ss
vsessiss
Jk
amFFS (4.72)
where,
2
ns
22
ns
s 21J (4.73)
Fsi = Force due to initial compression of suction valve in N
mes = Equivalent mass of suction reed in kg (Details are given in
Appendix 2 and Appendix 3)
avs = Acceleration of suction reed in m/s2
= Damping factor
The air enters the port in the valve plate axially, and flows through
the gap between the reed valve and the valve plate radially. Considering the
flow through the suction reed to be a nozzle flow, equation (4.74) can be used
to estimate the mass of air drawn in through the suction reed.
The mass of air entering during incremental angle (mos) is
calculated using
82
p
p1p
1n
2nVCCAm
ss 1)/n(n
es
eses
s
s2
oasdsfsos (4.74)
Suction area correction factor is given by
c
fsc
os
fsosas
A
AA
A
AAC (4.75)
The velocity of air at the outlet of the port using continuity equation
is obtained ass
p
os
c
oZ
V
A
AV (4.76)
The loss due to back flow on the suction side is estimated using
ss
2
ossbs ZSd4
m (4.77)
The total mass drawn-in per cycle is
bsos,os mmm (4.78)
Using improved valve dynamics the delivery valve lift as stated by
Piechna (1984) is estimated by
dd
vddidd
Jk
aFFS (4.79)
where,
2
nd
22
nd
d 21J (4.80)
83
= Damping factor
Fdi = Force due to initial compression of discharge valve in N
med = Equivalent mass of discharge reed in kg (Details are given
in Appendix 2 and Appendix 3)
avd = Acceleration of discharge reed in m/s2
The mass of air discharged during an incremental angle (mod) is
calculated using
p
p1p
1n
2nVCCAm
dd 1)/n(n
d
d
d2
oadddfddod (4.81)
Discharge area correction factor is given by
c
fdc
od
fdodad
A
AA
A
AAC (4.82)
where, Ac is the cylinder cross sectional area in m2.
The flow is taking place from the cylinder through the port, valve
and head. The above correction factor increases the flow area.
The velocity of air at the outlet of the port is
d
p
od
c
oZ
V
A
AV (4.83)
The loss due to back flow is estimated using dd
2
oddbd ZSd4
m (4.84)
where, d is the density of air during discharge process in kg/m3
Equation (4.84) is derived from, m = V
84
SdDelivery reed
Delivery reed Valve plate
The reverse flow of discharged air into the cylinder is shown in
Figure 4.10. Back flow reduces the amount of air discharged through the
delivery valve.
Figure 4.10 Back flow in reed valve
The total mass discharged per cycle is
bdod,od mmm (4.85)
4.6.4.3 Stage 3
In Stage 3 of MPD model the effect of head volume and blow-by
losses are considered.
The mass of air discharged from the suction head to the cylinder
(mohs) is estimated using
pp2CAm hsdhsohshsohs, (4.86)
where, hs is the density of air in the suction head in kg/m3, Aohs is the area of
orifice in the suction head in m2 and hs is the density of air in the suction
head in kg/m3, Cdhs is the coefficient of discharge for the port in suction head.
85
The coefficient of discharge for the port provided in the head is dependent on
head volume and diameter of port in the head. Werner Soedel (1976)
suggested the following equation to estimate the coefficient, Cdh:
)]ad(a[d/VaC 3oh2ohh1dh (4.87)
where, Vh is the volume of head, doh is the diameter of port in the head and a1,
a2 and a3 are the constants obtained from the experimental results of
refrigeration compressor. The value of a1 varies from 0.008 to 0.02, a2 from
0.45 to 0.55 and a3 from 0.0058 to 0.0064.
Therefore, the coefficient of discharge on the suction side for air
compressor is estimated as
0.0061)]d(0.513[d/V0.015C ohsohshssdh, (4.88)
The net mass in the suction head (mrhs, ) at any crankangle is given
by
os,ohs,1rhs,rhs, mmmm (4.89)
The temperature of air in the suction head (Ths, ) at any crankangle
is calculated using
rhs,
1hs,1ohs,os,1hs,1rhs,
hs,m
TmTmTmT (4.90)
The pressure of air in the suction head (phs, ) at any crankangle is
calculated using
86
hs
hs,rhs,
hs,V
RTmp (4.91)
The mass of air discharged from the delivery head to the reservoir
(mohd ) is estimated using
pp2CAm dhddhdohdhdohd, (4.92)
where, hd is the density of air in the head in kg/m3, Aohd is the area of the
orifice in the discharge head and Cdhd is the coefficient of discharge head
which is estimated using equation (4.87) with a1 = 0.01, a2 = 0.5 and
a3 = 0.006.
0.006)]d(0.5[d/V0.01C ohdohdhdddh, (4.93)
where, Vhd is the volume of air in the discharge head in m3 and dohd is the
diameter of orifice in the discharge head in m.
The mass remaining in the discharge head (mrh, ) at any crankangle
is given by
od,ohd,1rhd,rhd, mmmm (4.94)
The temperature of air in the discharge head at any crankangle
(Thd, ) is calculated using
rhd,
1hd,1ohd,od,1hd,1rhd,
hd,m
TmTmTmT (4.95)
87
The pressure of air in the discharge head (phd, ) at any crankangle is
calculated using
hd
hd,rhd,
hd,V
RTmp (4.96)
4.6.5 Suction process in Compressor 3
Compressor 3 employs ring valve on the suction side and reed
valve on the delivery side. Figure 4.11 shows the inlet valve assembly and
Figure 4.12 shows the delivery valve with valve plate used in Compressor 3.
Figure 4.11 Ring type inlet valve assembly
Figure 4.12 Delivery reed with valve plate
88
The air enters the port in the valve plate axially. Considering, the
flow through the suction valve to be an orifice flow, equation (4.97) can be
used to estimate the mass of air drawn in through the suction valve.
The mass of air entering during incremental angle (mos) iscalculated using,
)p(pVCAm hs
2
odsfsos, (4.97)
The inlet ring valve was tested for determining the stiffness (ks) at
different loads. Table 4.2 shows the stiffness of valve at different loads.
Table 4.2 Stiffness of ring valve at various loads
Load (N) Stiffness (N/mm)
0.18 0.50
0.56 0.53
0.93 0.56
1.31 0.60
1.68 0.65
2.07 0.71
2.25 0.74
An equation to determine the inlet valve stiffness has been
developed from the test results of the present work as given below. The
details are shown in Figure 4.13.
89
Figure 4.13 Variation of ring valve stiffness with load
4902.0F0429.0F0306.0k 2
s (4.97)
Using effective valve dynamics the deflection of suction valve is
estimated froms
vsssiss
k
amFFS (4.98)
4.6.6 Suction process in Compressor 4
Compressor 4 is a high speed and water cooled air compressor. It
employs ring valve on delivery and suction sides. There are 12 ports on the
suction side and 10 ports on the delivery side. The air leaves the port in the
valve plate axially. Considering the flow through the delivery valve as an
orifice flow, the mass of air leaving through the discharge port during
incremental angle is calculated using
)p(pVCAm hd
2
oddfdod, (4.99)
where, Vo is the velocity of air through the port in m/s.
90
4.7 FLOWCHART OF MATHEMATICAL MODEL
The mathematical model was coded with C++ program for
simulation analysis. The overall flowchart of algorithm for all the models is
shown in Figure 4.14. The flowcharts for various processes are given in
Appendix 4.
The compressor cycle is completed in 360o of crank rotation to
perform the suction, compression, discharge and re-expansion processes. For
the given set of input parameters, the model starts executing from
compression process. The step by step operations in the mathematical model
operation are as follows.
1. The angle ( d) at which the discharge starts is calculated.
2. The compression proceeds upto d from 180o (BDC) and
performance parameters are calculated during an incremental
crankangle.
3. After the crankangle d discharge process starts. The pressure,
temperature, mass of air discharged and all other parameters are
calculated at various crankangles.
4. The discharge continues upto 360o (TDC) of crank rotation.
5. The angle ( e) upto which the expansion of air in the clearance
volume continues is estimated.
6. The suction process starts from e and continues upto 180o.
7. The model is run several times upto the stabilisation condition is
achieved (the difference of any performance parameter between the
consecutive runs is within 0.01).
8. The output is obtained in text file and in excel file.
91
The important points to be considered while developing a
mathematical model of automotive air compressor were discussed in this
chapter. In addition, the development of actual compressor model from the
ideal model has also been explained. In Chapter 5 the details of experimental
set up with an error analysis on measured quantities are discussed.
92
Figure 4.14 Overall flowchart of mathematical model
START
Input Parameters
Calculate angle up to which expansion takes place and angle of start of delivery
Initiate the process by assigning theta=180
< d
Compression
Process
> d and
<360
Discharge Process
< e
Expansion process Suction Process= +
= +
= + = +
End
Check for stablisation
conditions
Transfer final conditions as initial
conditions
Output
<180
Yes NoNo No
92