Variational formulation of micropolar elasticity using 3D ...
Linear Stability Analysis of Hydrodynamic Journal Bearings with a Flexible Liner and Micropolar...
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Linear stability analysis of hydrodynamic journalbearings with a flexible liner and micropolarlubricationPikesh Bansala, Ajit K Chattopadhayaya & Vishnu P Agrawalba Mechanical Engineering Department, Faculty of Engineering and Technology, Mody Instituteof Technology and Science, Lakshmangarh332311, Rajasthan, Indiab Mechanical Engineering Department, Thapar University, Patiala147001, Punjab, IndiaAccepted author version posted online: 06 Oct 2014.
To cite this article: Pikesh Bansal, Ajit K Chattopadhayay & Vishnu P Agrawal (2014): Linear stability analysis of hydrodynamicjournal bearings with a flexible liner and micropolar lubrication, Tribology Transactions, DOI: 10.1080/10402004.2014.969817
To link to this article: http://dx.doi.org/10.1080/10402004.2014.969817
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Linear stability analysis of hydrodynamic journal bearings with a flexible liner and
micropolar lubrication
Pikesh Bansala, Ajit K Chattopadhayay
a, Vishnu P Agrawal
b
a Mechanical Engineering Department, Faculty of Engineering and Technology, Mody Institute
of Technology and Science,Lakshmangarh - 332311,Rajasthan, India
b Mechanical Engineering Department, Thapar University, Patiala-147001, Punjab, India
Abstract – A linear stability analysis of hydrodynamic journal bearings is presented, including
the effects of elastic distortion of the liner and micropolar lubrication. Hydrodynamic equations
of the lubricant and equations of motion of the journal are solved simultaneously with the
deformation equations for the bearing surface to predict the fluid film pressure distributions
theoretically. The components of stiffness and damping coefficients, critical mass parameter and
whirl ratio, which reflect the dynamic characteristic of the journal bearing, are calculated for
varying eccentricity ratio taking into account the flexibility of the liner and the micropolar
properties of the lubricant. The results presented show that stability decreases with an increase in
the value of the elasticity parameter of the bearing liner and micropolar fluids exhibit better
stability in comparison to Newtonian fluids.
Keywords
Micropolar Fluid; Hydrodynamic Lubrication; Elasticity of Liner; Non-Newtonian Behavior
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INRODUCTION
Hydrodynamic journal bearings are used for medium to large sized machinery such as steam and
gas turbines, generators, pumps and compressors due to their relatively long life. The best
operating conditions for hydrodynamic journal bearings are reached when they operate above a
certain minimum speed required to generate a fluid film of sufficient thickness such that metal to
metal contact can be avoided. Hydrodynamic journal bearings are subjected to excessive friction
and wear operated at lower speeds and especially during starting and stopping. As the cost of
replacing a bearing is high, these bearings are often provided with flexible liners so that only the
liners need to be replaced when damaged. There is a need to understand how the flexibility of the
bearing liner affects the maximum steady state pressure and the cavitation zone especially at high
values of eccentricity ratio.
Higginson (1) was the first to conduct research in this area in 1965. Since then many researchers
(2-17) have studied the performance characteristics of bearings with flexible liners. Further, all
of these studies were carried out assuming Newtonian behavior of the lubricant. The open
literature lacks sufficient design data on the effect of flexible bearing liners on the performance
of journal bearings operating with non-Newtonian lubricants.
Additives are used to enhance the performance of lubricants. The additives are polymeric in
nature while the bearing lubricants are often mineral based. Under normal working conditions,
lubricants become contaminated with wear debris. Henniker (18) found a tenfold increase in
viscosity within 5000 Å of the surface in his experiment of Couette type flow using leuben oil
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mixed with aluminium napthenate. Similar observations were made by Needs (19) in his
boundary lubrication experiments. These experimental results showed that classical continuum
theory was unable to predict the behavior of fluids in such conditions and generated a need for
new theory which could predict the behavior of such fluids.
The theory of micropolar fluids as discussed by Eringen (20) is based on microcontinua where
each material point of a continuum has six degrees of freedom, three rotational and three
translational. Nonsymmetrical stress tensors and couple stress are brought due to rotational
degree of freedom which are missing from the classical theory. Eringen (20) presented the
definition of micropolar fluids and a study of flow behavior of micropolar fluids in a circular
pipe. Micropolar fluids are fluids which consist of rigid, randomly oriented particles in a viscous
medium, where deformation of the fluid particles is ignored. An excellent review of various
theories of microcontinua is given by Ariman et al. (21). As evidenced by various investigators
(22-23), the theory of micropolar fluid may physically serve as a satisfactory model to predict the
behavior of polymeric fluids, real fluid suspensions, and flow through narrow channels like
animal blood.
Micropolar theory is applied to the problem of lubrication for two main reasons. First, the case
when lubricants are contaminated by residual metal particles and dirt under general operating
conditions falls in the domain of micropolar fluids as represented by fluids containing certain
suspensions and mixtures. Second, the clearance in bearings is of the order of an average grain
size of a non-Newtonian fluid. A practical application of the theory of micropolar fluids was
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given by Balaram (24) in the design of journal bearings in the area of nuclear power plants where
the heat transfer agent sodium is used as a lubricant and by Allen and Kline (25) in the case of
lubricant contamination with metal particles and dirt.
Early researchers (Shukla and Isa (26); Prakash and Sinha (27); Zaheeruddin and Isa (28); Tipei
(29)) discussed the effect of micropolar fluids on a one-dimensional bearing or mainly limited
their studies to infinitely long and short bearings. It was found that micropolar fluid theory was
capable of explaining certain phenomena encountered in lubrication problems like increased
effective viscosity as observed by Needs (19). Micropolar lubricants were observed to improve
bearing performance as evidenced by higher pressures, greater load carrying capacity and
increased side flow for the same bearing kinematics and geometry. Later, Singh and Sinha (30)
presented three-dimensional equations for bearings lubricated with micropolar fluids. A rigorous
mathematical analysis of micropolar fluid lubrication theory was presented by Bayada and
Lukaszewicz (31).
The performance characteristic of finite width journal bearing was investigated by Huang et al.
(32) and the performance analysis of a finite journal bearing was studied by Khonsari and Brewe
(33). However, Lin (34) investigated the effect of three dimensional irregularities on a
hydrodynamic journal bearing lubricated with micropolar fluids. Das, et al. (35-36) studied
conical whirl instability of a hydrodynamic journal and the steady state characteristics of
misaligned journal bearings lubricated with micropolar lubricants. Wang and Zhu (37) presented
a study on lubricating effectiveness of micropolar lubricants for a dynamically loaded journal
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bearing. Das et al. (38) studied the stability characteristics of a hydrodynamic journal bearing
under micropolar lubrication. Later, Das, et al. (39) presented a linear stability analysis for a
hydrodynamic journal bearing using micropolar lubricants. Wang and Zhu (40) discussed journal
bearing characteristics including thermal and cavitation effects with micropolar fluids as the
lubricant. Nair, et al. (41) investigated the static and dynamic performance characteristics of an
elastohydrodynamic journal bearing with micropolar fluids as the lubricant. Verma, et al. (42)
analyzed a multirecess hydrostatic journal bearing with micropolar lubricants. Nicodemus and
Sharma (43) presented the influence of wear on the performance of a multirecess hydrostatic
journal bearing with micropolar lubricants. Rahmatabadi, et al. (44) studied the effect of
micropolar lubricants on the performance characteristics of noncircular lobed bearings.
Naduvinamani and Santosh (45) studied squeeze film lubrication of finite porous journal
bearings with micropolar lubricants. Nicodemus and Sharma (46) studied the performance
characteristics of a micropolar lubricated membrane compensated worn hybrid journal bearing.
Lin, et al. (47) studied the dynamic characteristics of parabolic film slider bearings with
micropolar fluids as lubricants. Quite recently, Sharma and Rajput (48) investigated the effect of
geometric imperfections of a journal on a 4-pocket hybrid journal bearing using micropolar
fluids as a lubricant.
There is a lack of information in the literature addressing the stability analysis of journal
bearings with flexible liner under micropolar lubrication. The aim of the present study is to
explore analytically the effect of micropolar lubricants on the linear stability of journal bearings
with flexible liners as shown in Fig 1. First, deformation of the flexible liner is calculated by
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solving displacement components in the elastic medium as discussed by Oh Huebner (6),
Conway and Lee (7), and Majumdar, et al. (10). Deformation of the flexible liner is used to
calculate fluid film thickness which is then used to calculate film pressure by solving the
modified Reynolds equation for micropolar lubricants as discussed in the literature survey (32-
48). Using a first order perturbation, the pressure is converted to steady-state and dynamic
pressures. Stiffness and damping components are calculated from these pressures which are used
in the equation of motion to obtain the mass parameter and whirl ratio. A parametric study is
conducted for linear stability analysis of a journal bearing with a flexible liner lubricated by a
micropolar fluid. However, due to a dearth of literature regarding actual values of micropolar
parameters, the values assumed by previous researchers (32-48) were used in present study.
Kolpashchikov, et al. (49) attempted to calculate the values of micropolar parameters by taking
data for water flow in capillaries from Deryagin, et al. (50). In the absence of experimental data,
the theoretical mass parameter obtained by this analysis has been compared with available
results. The results presented herein are expected to be useful for practicing engineers in the field
of bearing design and as well as for academicians.
ANALYSIS
Figure 1 shows a schematic diagram of a journal bearing with a flexible liner. The elliptical path
of the journal has a major axis Cε0 1 and a minor axis Cε1.
Modified Reynolds Equation
The modified Reynolds equation (Prakash and Sinha (27), Singh and Sinha (30)) for journal
bearings lubricated with micropolar fluids with assumptions to generalize the micropolar effect
(Prakash and Sinha (27), Singh and Sinha (30)) for linear stability analysis is
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3 3p ph h 2 h h
,N,h ,N,h 6U 1 12x x z z t x t
[1]
where
1/ 2 1/ 22
2
N Nh( , N,h) 1 12 6 coth , , N
h 2 4 2h
The parameter η represents the viscosity of the Newtonian fluid. γ and χ are the material
coefficient and spin viscosity, respectively for the micropolar fluid. The film thickness is h and
the micropolar film pressure for the bearing is p. Λ and N are two parameters which are
associated with the micropolar fluid and are used to distinguish the micropolar fluid from a
Newtonian fluid. Λ is termed the characteristic length of the micropolar fluid, representing the
interaction between the film gap and the micropolar fluid. As Λ tends to zero the modified
Reynolds equation is reduced to the usual Reynolds equation for a Newtonian fluid. N is termed
the coupling number and is a dimensionless number which couples the linear and angular
momentum equations which arise as a result of the microrotational effect of the suspended
particles such as additives, dirt, and metal particles in the fluid.
Equation [1] will be reduced to its non-dimensional form as
2
'
m m
p D p 1 h hg l , N,h g(l , N,h) 1 2
L z z 2 t
[2]
with the following substitutions
2
m2
x 2z h pC C, z ,h , p , l , t t
R L C R
where,
3 l Nhh h Nh mg l , N, h coth
m 212 2l 2l mm
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and
'
t
In the case of a flexible bearing, the steady state film thickness h is given by (O’Donoghue, et al.
(3) and Majumdar, et al. (10))
h 1 cos [3]
h eh , ,
C C C
δ, represents the radial deformation of the bearing liner surface.
For a flexible bearing, the non-dimensional radial deformation is first obtained before trying to
find the solution of equation [2]. The method of calculating elastic deformation is as suggested
by Brighton, et al. (4) and Majumdar, et al. (10). Satisfying the boundary conditions, the three
displacement components u, v and w are calculated. The method is briefly explained below.
The non-dimensional radial deformation of the bearing liner surface can be calculated as
suggested by O’Donoghue, et al. (3) and Majumdar, et al. (10) using:
m,n m,n m,n
m 0 n 0
2m z2 1 F p d cos cos n
L
[4]
3
3
RF
EC
F is defined as the deformation factor which gives a measure of the relative magnitude of viscous
shear stress compared with the normal stress per unit normal strain for the bearing liner material
in the radial direction for a particular bearing geometry. The Poisson’s ratio for the bearing liner
material is ν.
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To calculate the values of pm,n and βm,n, the two-dimensional modified Reynolds equation is
solved to obtain pressure distribution assuming the bearing is rigid and assuming steady state
conditions. This pressure distribution is expressed as a double Fourier series. (O’Donoghue (3)
and Majumdar, et al. (10))
2m z| |p p cos cos n
m n m,n m,nL
[5]
where |
indicates that the first term of the series is halved, and m,n and m,n are calculated as
follows
2 22 1 2 1
m,,n
0 0 0 0
2p cos m z cos n dzd p cos m z sin n dzd
Lp
[6]
2 1
1 0 0
m,n 2 1
0 0
p cos m z sin n dzd
tan
p cos m z cos n dzd
and 2 1
0,0
0 0
1p pd dz
where 2 2
m,n
m,n 2 2
p C pC zp , p , z
L / 2R R
To calculate dm,n, three displacement components in r, θ, z can be assumed as (Mazumder (52))
r m,n
m,n
z m,n
2m zu u a cos(n )cos
L2m z
u v a sin(n )cosL
2m zu w a cos(n )sin
L
[7]
where u , v and w are functions of r only and a is the inside radius of the bearing liner.
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The stress displacement relationship, Mazumder (52) and Rekach(53), gives
r z r
rr
r z
r
r z z
zz
r
r
z
z
u(ru ) u u1 12
r r r z ru u(ru ) u1 1
2 ur r r z r
u(ru ) u u1 12
r r r z z
uu1r
r r r
u u1
z r
z r
zr
u u
r z
[8]
The equations of equilibrium from the basic theory of elasticity can be written as (Mazumder
(52) and Rekach (53))
r rrrr rz
r z r
zrz zz rz
10
r r z r1
2 0r r z r
10
r r z r
[9]
Substituting the values of ur, uθ and uz from equation [7] in the stress-displacement equations [8]
then further substituting the stress components in the equilibrium equations [9] gives following
relations:
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22
2 2
2
2
22 2
2 2
2
2
2
d u C du u n dvC (C n ) (C 1)
y dy y dydy yn dw
(C 1) v k u (C 1)k 0dyy
d v 1 dv v n du(1 C n ) k v (C 1)
y dy y dydy yn w
(C 1) u nk(C 1) 0yy
d w
dy
22
2
1 dw n duw C k w (C 1)k
y dy dyyu v
k(C 1) nk(C 1) 0y y
[10]
2 ma r E EC 2 ,k , y , ,
L a (1 )(1 2 ) 2 1
The boundary conditions are (Majumdar(10) and Mazumder (52))
1. The ends of the bearing are prevented from expanding axially, but are free to move
circumferentially or radially.
m,n
du 1 nv uy 1,C p (C 2)( kw )
dy y ydv nu v
dy y y
dw u k
dy
[11]
2. The outer surface of the bearing is rigidly enclosed by the housing, preventing any
displacement of the outer surface.
bat y= , u =v =w =0
a
First u is calculated by solving equation [10], taking into consideration the boundary conditions
in equation [11] with value of pressure as unity. Next, dm,n is calculated using equation given
below.
m,n
ud =
Rp
[12]
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Perturbation Method
Non-dimensional pressure and film thickness are calculated using a first order perturbation
technique with the assumption that the journal whirls about its mean steady position given by the
eccentricity ratio ε0 with amplitudes Re i t1e
and Re i t
0 1e along the line of centers and
perpendicular to the line of centers respectively. The non-dimensional pressure and local film
thickness are
i t i tp p p e p e0 1 1 2 0 1
i t i th h e cos e sin0 1 0 1
[13]
where
i th 1 cos , e0 0 0 1
pi te and 0 1
[14]
The subscript i = 0, 1 and 2 represents pressures for steady state and first order perturbations in
Eqs.[12]-[14], respectively (Das et al. (39)).
Equation for Steady-State and Dynamic Conditions
Expanding Equation [2] with all the substitutions made and by neglecting higher order terms of
(ε1) and (ε0 1), the following three equations are obtained by collecting the zeroth and first order
terms of ε1 and ε0 1
2 22 2
0 0 0 0 0 0 0
1 2 2 2
h p h p p p hD D 1C C
L z z L 2z
[15]
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2 2 22 22 2
0 0 0 01 1 1 12 1 12 2 2 2
2 2
0 0 01 1
3 1
p p h hp p p pD D DC C cos C
L L L z zz z
h h pp pD D pC cos C sin cos
L z z L z
1sin i cos
2
[16]
2 2 22 22 2
0 0 0 02 2 2 2
2 1 12 2 2 2
2 2
0 0 0 02 2
3 1
p p h hp p p pD D DC C sin C
L L L z zz z
h h p pp pD DC sin C cos sin
L z z L z
0
0
h1 icos i sin
2
[17]
where,
2 2 2
20 0 m 0 0 m 0
1 2
mm
h Nh Nl h N h Nl h1C coth cosech
4 l 2 4 2l
3 2
0 0 0 m 0
2 2
mm
h h Nh Nl hC coth
12 2l 2l
3 2
2 2 20 m 0 m 0 m 0 m 0 m 0
3 0
m
h Nl h Nl h N l h Nl h Nl hNC N h cosech coth cosech coth
2 2 l 2 4 2 2
Boundary Conditions
The boundary conditions relevant to the problem are as follows:
1. The steady state pressures and perturbed pressures at the ends of the bearing are zero
p ( ,z) 0, i 0,1,2 at z= 1i
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2. The pressure distribution is symmetrical about the mid-plane for steady state pressures
and perturbed pressures of the bearing
p ,z
i 0, i 0,1,2 at z=0z
3. Cavitation boundary conditions
1
p ( ,z)0 2p ( ,z) 0
0 2 zp ( ,z) 0, i 0,1,2 for
2i
where θ1 and θ2 represent, respectively, the angular coordinates where the film starts and
the film cavitates. The cavitation boundary condition is replaced by the method of
constraints suggested by Christopherson (54) to facilitate computation while economizing
time.
4. Periodic boundary conditions
p ,z p ( 2 ,z), i 0,1,2i i
Steady State Load
The components of the fluid film force in non-dimensional forms along the line of centers and
perpendicular to the line of centers are
2
1
2
1
1
R 000
1
000
F p cos d dz
F p sin d dz
[18]
Utilizing the above non-dimensional fluid film force components, the non-dimensional steady
state load, attitude angle and the Sommerfeld number are obtained.
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1/ 222
0 R 0 0
1 0
0
R 0
0
W F F
Ftan
F
1S
w
[19]
where
2
0
0 3
2W CW
R L
Stiffness and Damping Coefficients
Non-dimensional components of stiffness and damping coefficients can be calculated from the
dynamic film pressures as follows (Majumdar, et al. (10))
2
1
2
1
2
1
2
1
2
1
2
1
1
RR 1
0
1
R 1
0
1
R 2
0
1
2
0
1
RR 1
0
1
R 1
0
S Re 2 p cos d dz
S Re 2 p sin d dz
S Re 2 p cos d dz
S Re 2 p sin d dz
ImD 2 p cos d dz
ImD 2 p sin d dz
2
1
2
1
1
R 2
0
1
2
0
ImD 2 p cos d dz
ImD 2 p sin d dz
[20]
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Equations of Motion
Considering the rotor to be rigid, the equations of motion of the journal along the line joining
centers and in the direction perpendicular to it, can be written as (Majumdar, et al. (10))
22
R2
d dMC F W cos
dtdt
[21]
2
2
d d dMC 2 F Wsin
dt dtdt
[22]
where FR and F are the resultant film forces in the R and directions, respectively.
For the steady state condition (Majumdar et al. (10))
R 0 0 0 00 0F W cos 0 and F W sin 0 [23]
Substituting equations [14] and [23] into equations [21] and [22] and non-dimensionalising with
the following substitutions
3 3
ij ij ij ij3 3
2C 2CS S ;D D ;
R L R L
2 2
0 03
0
2C MCW W ;M ;
WR L
and retaining only the first order terms gives the non-dimensional equations of motion
(Majumdar et al. (10))
2
0 RR RR 1
0 R 0 R 0 0 1
MW S i D
S i D W sin 0
[24]
2S i D MWR R 1 0 0
S i D W cos 00 0 0 0 1
[25]
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For a non-trivial solution, the determinant of the coefficient matrix of equation [24] and equation
[25] must vanish. When the imaginary and real terms of the determinant are equated to zero
separately, the following two equations are generated (Majumdar et al. (10))
0
0 RR RR R R R R R 0 RR 02
0RR
W1MW S D S D S D S D (D sin D cos )
(D D )
[26]
2 4 20 0
0 0 RR RR R R RR R R
0
0
RR 0 R 0
0
W cosMW MW S S D D D D S S S S
WS cos S sin 0
[27]
Whirl ratio and mass parameter can be calculated from the above two equations.
METHOD OF SOLUTION
The dimensionless stability parameter for a journal bearing with a flexible liner with micropolar
lubrication is obtained via the following procedure.
1. Initialize the values of the input parameters i.e. L/D, H/R, ν, F, ε0, lm, N2, over relaxation
factors, convergence criterion and number of maximum iterations.
2. Initialize iteration number n to 0.
3. Initialize dimensionless steady state pressureijp 0 .
4. Calculate dimensionless film thickness assuming non-dimensional radial deformation of
bearing liner surface =0.
5. Solve equation [15] in finite difference form using a successive over relaxation scheme
satisfying boundary conditions and taking film thickness as calculated in step 4. This step is
repeated iteratively until convergence is achieved or number of maximum iteration is
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exceeded. If the maximum iteration number is exceeded, change the over relaxation factor
and go to step 2 and repeat until convergence is achieved.
6. The pressure profile generated in step 5 is expressed as a double Fourier series as given in
equation [5]. Then m,,np and m,n are calculated by Simpson’s 1/3
rd rule.
7. Values of dm,n are calculated by solving equation [10] for unit pressure, and μ and R by the
finite difference method (Gauss-Seidel iteration) with a successive over relaxation scheme.
These values of dm,n are stored in computer memory for further use.
8. is calculated by substituting the values of dm,n, m,,np and m,n in equation [4].
9. Using these values of , calculate a new dimensionless film thickness from step 4. Repeat
the procedure until convergence is achieved to obtain final steady state pressure profile.
10. Similarly solve equations [16] and [17] to get perturbed pressure along the line joining the
centers and perpendicular to the line joining the centers.
11. Calculate steady state load from equation [16] using the components force in the direction of
the line of centers and perpendicular to the line of centers which are calculated by Simpson’s
1/3rd
rule. Calculate the stiffness and damping coefficients by Simpson’s 1/3rd
rule using
equation [20].
12. Use the these values calculated in steps 10 and 11 in equations [26] and [27] to obtain the
mass parameter and whirl ratio. Equations [26] and [27] are solved to get whirl ratio. If the
roots of the whirl ratio are real, the mass parameter is obtained using equation [26]. If the
roots are imaginary, then the equilibrium position is stable.
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RESULT AND DISCUSSIONS
In this paper, the dynamic characteristics for a journal bearing in terms of critical mass parameter
and whirl ratio are computed considering the flexibility of the bearing liner and micropolar
lubrication. The critical mass parameter (a measure of stability) is the threshold value of M above
which the bearing will be unstable. The journal speed corresponding to the critical mass
parameter is the threshold speed. Whirl ratio gives the ratio of frequency of the center trajectory
with respect to spin of the journal. Whirl ratio helps diagnose whether self excited vibration is
due to oil or synchronous whirl. Since the critical mass parameter and whirl ratio are dependent
on steady state and perturbed pressure and thus, in turn are functions of lm, N2 and F, a
parametric study is done to show the effect of these parameters on critical mass parameter and
whirl ratio. The components of stiffness and damping coefficients are used to calculate the
critical mass parameter and whirl ratio, so their variation is not shown.
In order to validate the computer program developed and the solution algorithm the results were
compared with published results. The mass parameter for journal bearings with a flexible liner
using a Newtonian fluid as a lubricant is compared with that obtained by Mazumdar, et al. (10)
as shown in Figure 2. Also the results for the mass parameter for the case of a rigid bearing
lubricated by a micropolar fluid are compared with Das, et al. (39) as shown in Figure 3. The
results shown in Figure 2 and Figure 3 compare well, agreeing with in 4-7%.
The critical mass parameter and whirl ratio are calculated for various values of ε0 (0.6-0.85),
Sommerfeld Number (0-0.35), lm (10-80), N2 (0.1-0.9), F (0.0-0.5), H/R = 0.3, ν = 0.4, L/D =1.0.
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Constant values of H/R, L/D, ν are used in order to compare the results with Majumdar et al.
(10). Values of ε0 above 0.6 are considered since the effect of the flexibility of the liner is
negligible below ε0 = 0.6, as predicted by Majumdar, et al. (10) and Brighton, et al. (4). The
values of lm and N2 can be determined experimentally as shown by Kolpashchikov et al. (49).
Table 1 (55) gives the values for lm and N2 as calculated by Pietal (55) for exemplifying fluids
whose chemical composition is given in detail in (56, 57). Due to limited data available for
values of micropolar parameters lm and N2 for real fluids, the values used herein are the same as
those taken by other researchers in the field of micropolar lubricants (32-48), considering that all
the real fluids working as lubricants will have values in the range provided.
Figure 4 shows the variation of the critical mass parameter versus Sommerfeld number. The
graph shows how the mass parameter is affected by the elasticity parameter F of the bearing liner
when considering a micropolar fluid as the lubricant, a bearing geometry of L/D = 1.0, ν=0.4,
H/R=0.3, and micropolar parameters of lm=40.0 and N2=0.5. The graph clearly shows that as the
value of the elasticity parameter increases from 0.0 to 0.4 the stability of the bearing tends to
decrease. The elasticity parameter is inversely proportional to the Young’s modulus. So, the
stability of the bearing will increase when a bearing liner with a higher value of Young’s
modulus is chosen.
Figure 5 shows a parametric study of the effect of the characteristic length of the micropolar
fluid on the critical mass parameter for L/D=1.0, ν=0.4, F=0.2, H/R=0.3 and N2=0.5. The
variation of the plot exhibits typical trends for critical mass parameter versus Sommerfeld
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number curves for a Newtonian fluid but the micropolar fluid shows a higher stability threshold.
As lm→∞ the stability threshold shifts towards that of the Newtonian fluids. This is due to the
fact that lm represents the characteristic length of the substructure and as lm→∞, the fluid loses its
micropolar characteristics and is reduced to a Newtonian fluid.
Figure 6 shows the combined effect of the elasticity parameter F and the characteristic length. In
this graph the critical mass parameter is plotted against lm for various values of F. There are two
important observations. First, the value of the critical mass parameter is maximum as the value
of lm→10.0. Second, the value of the critical mass parameter decreases as the value of F
increases.
The variation of the critical mass parameter versus the elasticity parameter is shown in Figure 7
for various values of eccentricity ratio at L/D=1.0, ν=0.4, H/R=0.3, lm=40.0, N2=0.5. The
variation in the graph depicts that the value of critical mass parameter decreases as the value of
elasticity parameter is increased from 0.0 to 0.5. The value of the critical mass parameter
decreases rapidly for ε0=0.85 and goes below values of the critical mass parameter for ε0=0.8.
This is due to the fact that as F increases also increases, which in turn increases minimum film
thickness. Due to an increase in minimum film thickness there is a reduction in pressure and
hence lower values of the critical mass parameter. Similar observations were made by Conway
and Lee (7) using the short bearing approximation and by Majumdar, et al. (10) using a finite
bearing. The value of the critical mass parameter decreases sharply as the value of the elasticity
parameter increases from 0.0 to 0.1.
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The variation of whirl ratio versus non-dimensional characteristic length lm for various values of
the elasticity parameter F for L/D=1.0, ν=0.4, H/R=0.3, ε0=0.5, N2=0.5 is shown in Figure 8. The
value of whirl ratio increases as the value of F is increased up to F = 0.2, but is found to decrease
with further increase in value of F for a given value of lm. However, the values of whirl ratio are
taken at an accuracy of 10-4
in order to show the variation and the values in all cases lie in a
range between 0.52 and 0.56.
Figure 9 shows the variation of whirl ratio versus the elasticity parameter F for various values of
ε0 at L/D=1.0, ν=0.4, H/R=0.3, lm=40.0, N2=0.5. The graph indicates that the variation of whirl
ratio for ε0=0.6 and 0.8 (0.43 < <0.53) is not significant as the value of F is increased but the
value of whirl ratio increases drastically (0.31 < < 0.53) for ε0 = 0.85 as the value of F is
increased. This increase is also due to the fact that the pressure profile reduces as F is increased
due to an increase in minimum film thickness.
CONCLUSION
From the above study it can be concluded that
1) The performance characteristics of a journal bearing with a flexible liner are significantly
affected by the flexibility of the liner and the micropolar effect of the lubricant. The effect of
the flexibility of the liner should be taken into account especially at higher eccentricity ratio
(i.e. ε0≥0.8) in order to accurately predict the performance characteristics.
2) When a bearing liner is used, the designer should choose a liner material with a high Young’s
modulus to achieve better stability, especially when the bearing is operating at high
eccentricity ratio (i.e. ε0≥0.8).
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3) The stability parameter improves for any value of elasticity parameter for micropolar
lubricated bearings in comparison to bearings lubricated with Newtonian fluids. The
maximum effect of micropolar fluids is observed when lm→10.0.
4) An increase in the micropolar characteristics of a fluid increases stability while an increase in
the deformation factor of the liner reduces stability. An optimized solution may be created
when designing a journal bearing with a flexible liner.
5) The whirl ratio for journal bearings using a flexible liner remains near 0.5. However, the value
of whirl ratio may vary from 0.3 to 0.5 at higher eccentricity ratios (i.e. ε0≥0.8).
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Nomenclature
a, b inside and outside radius of bearing
liner (m) t, t
U time (s), t t
velocity of the journal (m/s), U = ωR
C radial clearance (m) Ω whirl ratio
C' 2+λ/μ W0, 0W steady state load (N), 2 3
0 0W 2W C R L
D journal diameter (m) α constant describing the fluid-wall
interaction
Dij, ijD damping coefficient of micropolar
fluid for i = R, and j = R, (Ns/m), 3 3
ij ijD 2D C R L
x, y, z
θ, y , z
circumferential, radial, axial
coordinates (m)
dimensionless coordinates, θ=x/R,
dm,n distortion of m, n harmonic y y a , z z /(L / 2)
E Young’s modulus (N/m2) u', v', w' radial, circumferential and axial
e, ε steady state eccentricity at mid-plane displacements
of bearing (z=0) (m),ε = e/C η viscosity of Newtonian fluid (Pa s)
F deformation factor, 3 3F R C E γ, χ viscosity coefficient for the micropolar
Fi force component along the R and
directions for i = R and (N)
τij
fluid (Pa s)
stress in ith plane in jth direction (N/m2)
H = b-a
h, h
thickness of bearing liner (m)
local film thickness (m), h h C
δ, radial deformation at bearing liner
surface (m), C
Λ
ν
characteristic length of the micropolar
fluid (m)
Poisson’s ratio
ω
ωp
angular velocity of the journal (rad/s)
angular velocity of orbital motion of
the centre (rad/s)
lm non-dimensional characteristic length
of micropolar fluid (m), lm=C/Λ
λ, μ
Lame’s constant
attitude angle (rad)
L bearing length (m) θ angular coordinate of the bearing (rad)
m, n
M, M
CM
axial and circumferential harmonic
mass parameter (kg), 2
0M MC W
critical value of non-dimensional mass
θ1, θ2 angles of end and start of
hydrodynamic film at each axial plane
of bearing (rad)
N
p, p
parameter
coupling number
local film pressure (Pa), 2 2p pC R
¯
S
above a variable represents the non-
dimensional value of parameter
Sommerfeld number
R
Sij, ijS
journal radius (m)
stiffness coefficient of micropolar
0
subscript represents the steady state
value
fluid for i = R, and j = R, (N/m), 3 3
ij ijS 2S C R L
1 and 2 subscript represents the first order
perturbation along ε0 and directions
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1. Solid Housing 2. Flexible Liner 3. Journal 4. Lines of centers
Fig. 1 Schematic diagram of Journal Bearing
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Fig. 2 Variation of critical mass parameter versus F taking Newtonian fluid as lubricant
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Fig. 3 Variation of critical mass parameter as a function of lm for Rigid Bearing taking
micropolar fluid as lubricant for various values of N2 at ε0 = 0.5 and L/D = 1.0
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Fig. 4 Variation of critical mass parameter as a function of Sommerfeld number for various
values of F at L/D =1.0, ν=0.4, lm=40.0, N2=0.5, H/R=0.3
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Fig. 5 Variation of critical mass parameter as a function of Sommerfeld number for various
values of lm at L/D=1.0, ν=0.4, F=0.2, H/R=0.3, N2=0.5
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Fig. 6 Variation of critical mass parameter with respect to lm for various values of F at L/D=1.0,
ν=0.4, H/R=0.3, ε0=0.5, N2=0.5
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Fig. 7 Variation of critical mass parameter versus F for various values of ε0 at L/D=1.0, ν=0.4,
H/R=0.3, lm=40.0, N2=0.5
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Fig. 8 Variation of whirl ratio versus lm for various values of F at L/D=1.0, ν=0.4, H/R=0.3,
ε0=0.5, N2=0.5
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Fig. 9 Variation of whirl ratio with F for various values of ε0 at L/D=1.0, ν=0.4, H/R=0.3,
lm=40.0, N2=0.5
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Table 1 Values of parameters Λ and N of some fluids
Fluid Λ, m. N
α = 0 α = 0.9 α = 0 α = 0.9
P1 3.34095 x 10−9 5.79745 x 10−9 0.50782 0.88921
P2 6.1088 x 10−9 1.022 x 10−8 0.53432 0.89443
water 9.2614 x 10−9 1.3392 x 10−8 0.6483 0.93744
E1 1.2713 x 10−5 1.867 x 10−5 0.63565 0.93352
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