eccentricity measurements on a five-pad tilting pad journal bearing · · 2015-10-15eccentricity...
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The 14th IFToMM World Congress, Taipei, Taiwan, October 25-30, 2015 DOI Number: 10.6567/IFToMM.14TH.WC.OS14.020
Eccentricity Measurements on a Five-pad Tilting Pad Journal Bearing
Phuoc Vinh Dang1
Politecnico di Milano
Via La Masa 1, I-20156 Milan, Italy
Steven Chatterton2
Politecnico di Milano
Via La Masa 1, I-20156 Milan, Italy
Paolo Pennacchi3
Politecnico di Milano
Via La Masa 1, I-20156 Milan, Italy
Andrea Vania4
Politecnico di Milano
Via La Masa 1, I-20156 Milan, Italy
Filippo Cangioli5
Politecnico di Milano
Via La Masa 1, I-20156 Milan, Italy
Abstract: The study of static and dynamic effects plays a
key–role in the field of rotor dynamics to evaluate the
behavior of hydrodynamic bearings. This paper describes
an experimental apparatus and the procedure for
measuring the static eccentricities and the bearing
clearance distribution in a five–pads tilting pad journal
bearing (TPJB). The tests have been carried out on a five–
pads TPJB with nominal diameter of 100 mm, length–to–
diameter ratio (L/D) of 0.7 and load–on–pad (LOP)
configuration. The results show that the clearance profile,
with a pentagon–shape, is a function of the operating
temperature and of the pad dimensions. Besides, the
barycenter of the clearance profile is very close to the
equilibrium position of the journal center at low rotational
speeds. A procedure for the evaluation of the bearing
clearance with experimental measurement is also
described. Keywords: Tilting pad journal bearing, eccentricity, clearance
profile, bearing clearance, load-on-pad
I. Introduction
It is well known that dynamics of high–speed rotating
machines strongly depends on journal bearing
characteristics. Currently, the titling pad journal bearings
(TPJBs) are widely mounted on high rotational speeds
machinery, such as steam and gas turbines. This is mainly
due to two special features of the TPJBs, which are i)
stability at high rotational speeds and ii) tolerance to
misalignment.
In order to select and design TPJBs compatible with
the required operating conditions of a high–performance
rotating machine, analytical models are commonly used to
forecast, among others, the white–metal temperature, the
load capacity, the minimum oil–film thickness, the
stiffness and the damping coefficients. However, it is
difficult to exactly predict the performances of a TPJB
because of its complex geometry, model uncertainties (in
particular about pivot compliance), large oil temperature
variations, and possible establishment of turbulent flow in
the oil–film.
[email protected] 2steven.chatterton@ polimi.it [email protected] 4andrea.vania@ polimi.it 5filippo.cangioli@ polimi.it
A theoretical study about the effects of TPJB
geometry, on the static and the dynamic characteristics,
has been presented by Jones and Martin [1], by considering
the load direction, the pad clearance, the bearing clearance,
the length–to–diameter ratio and the number of pads
The effects of eccentricity of the journal have been
studied in [2] and [3] for a circular bearing and in [4] for a
TPJB. Good agreements have been obtained between
measured and theoretical eccentricities, for a range of
Sommerfeld numbers between 0.2 and 3.0.
Walton and San Andrés [5] have provided some
experimental results of the static and dynamic
performances of a TPJB with flexible pivot. The
measurements have been employed to validate the
analytical simulations performed on this kind of bearing.
In addition, the phenomena related to heat transfer were
evaluated experimentally to provide an estimation of the
bearing power losses, during operation. The test conditions
consisted of rotational speeds and static loads up to 4,500
rpm and about 1,400 N (311 lbf), respectively. The cross–
coupling effects resulted relatively negligible for this
bearing type, over the range of loads and speeds tested, due
to the small pad displacements in the orthogonal direction
to the applied load. Moreover, a very little sub–
synchronous oil–whirl, was observed within the bearing
during the tests. Besides, the bearing stiffness increased
with the increasing of either the applied static load for a
given journal rotational speed or the journal rotational
speed for a constant load.
Wilkes and Childs [6] have investigated the effects of
the oil temperature, the pad clearance and the radial
displacement of the loaded pad (i.e. the pad having the
static load vector directed through its pivot) on the bearing
clearance. The measured clearances corresponding to
thermal steady state were approximately 30% smaller than
the measured one at the cold start–up and were inversely
proportional to pad surface temperature.
The aim of this paper is to present the results of the
measurements of eccentricity, clearance profile and
bearing assembled clearance Cb in a 100 mm diameter,
length–to–diameter ratio of 0.7, LOP configuration five–
pads TPJB. It is observed that both the actual machined
geometry and the pad assembling cause the clearance
profile to be far from the ideal design one. This could
affect the actual characteristics of the TPJB, also including
the existence of cross–coupling effects.
II. Description of the test rig and of the bearing
A detailed description of the test–rig, used for the
experimental tests is given in [7, 8, 9]. The rotor is
supported by two equal TPJBs, with nominal diameter of
100 mm and length-to-diameter ratio of 0.7. The bearing at
the non-driven end (NDE) which is labeled 1 of the shaft is
tested. The load is applied in the middle of the shaft by
means of two hydraulic actuators arranged in an
orthogonal configuration at ±45° with respect to the load
cells. The actuators are connected to the shaft by means of
two deep-groove high-precision ball bearings. Thanks to
this configuration, both the static load and the dynamic
loads can be applied in any direction. The nominal force of
the hydraulic actuator is 25 kN. The actuators are able to
move the shaft with amplitude of 100 µm in the frequency
band of 0-50 Hz and are provided by high-resolution
position and force transducers. The test-rig is controlled by
proprietary PC-based software, while data acquisition is
performed by means of Labview software and PCI DAQ
boards (National Instruments cDAQ-9178). A sketch of the
test–rig is shown in Fig. 1.
Fig. 1. Test-rig used for identification of
bearing characteristics
All the pads are instrumented with a temperature
sensor and a pressure probe, as shown in Fig. 2. The
pressure probe measures the pressure in the center of the
pad by means of a tiny hole in the white–metal and a duct
in the shoe. The geometric characteristics of the bearing
under test and the operating conditions are listed in Table
1. A picture of the complete test–rig is shown in Fig. 3.
Fig. 2. Five-pads tilting pad journal bearing
used for the tests
Item Unit Value/Span
Number of pad - 5
Configuration w.r.t
bearing housing - LOP
Bearing diameter (D) mm 100
Machined clearance (Cp) mm 0.125
Nominal pads thickness mm 16.0
Bearing length (L) mm 70
Angular amplitude of pads degrees (°) 60
Upper pads - 3,4
Lower pads - 1,2,5
Lubricant - ISO VG46
Rotational speed rpm 1200
Static load
(on each bearing) kN 5
Table 1. Bearing geometric characteristics
and operating conditions
Fig. 3. Picture of test-rig used to perform the
tests
Motor Ball
bearing
Hydraulic
actuator
2
1
Hydraulic actuator
Load
cell
Pressureprobe
Temperatureprobe
Nozzle
Pressure
probe
Temperature
probe
III. Experimental procedure
The experimental results discussed here have been
obtained with the load centered over the bottom bearing
pad, i.e. in the LOP configuration.
Since the thermal expansion of the bearing housing,
which supports the proximity probes, makes it difficult to
define the actual center of the bearing, steady–state shaft
eccentricities have been measured with respect to a lightly
loaded equilibrium position, corresponding to the shaft
rotating at 50 Hz (3000 rpm) with the external load equal
to about 350 N on each bearing. The Sommerfeld number
for this lightly loaded equilibrium position, which
corresponds to an eccentricity ratio less than 0.01, is
greater than 12 [10]. We can consider this position as the
bearing center. The Sommerfeld number is calculated
using the following formula:
2
p
NLD RS
W C
(1)
where:
µ: oil dynamic viscosity [Pa s], in which ( )T
N: shaft rotational speed [Hz]
L: bearing length [m]
D: bearing diameter [m]
R: bearing radius [m]
Cp: machined clearance [m]
W: vertical load applied on the bearing [N]
The dynamic viscosity, µ, is interpolated from the
curve of dynamic viscosity vs. temperature.
The average temperature over the five pads, measured
on the centerline position for each pad, is calculated as:
1
1
n
pad i
i
Pad temp Tn
(2)
where:
n: number of pads (n = 5)
Tpad-i: temperature of i-th pad
The average temperature is assumed as the actual
temperature of oil–film. The actual oil–film temperature
and corresponding viscosity are used for the calculation of
the Sommerfeld number.
Before and after each test run, once the rotation had
stopped, the clearance profiles of bearing were measured
by using the proximity probes. The rotor is slowly moved
inside of the housing support by means of a rotating force,
applied in the middle of the shaft through the deep groove
precision ball bearings and the two hydraulic actuators [7].
The rotating resultant force has been chosen in order to:
ensure that each pad is loaded by the exerted thrust
along its span;
be sufficiently high to put the shaft in contact with
all the pads;
to prevent significant pivot deflections during the
tests.
The temperature of the oil is kept at 40°C by means of
a PID temperature controller. However, in correspondence
of bearing loads that are extremely high or low, the
temperature may exceed this limit.
After having obtained the clearance profile of the
bearing, using interpolation, five points at the vertices of
the pentagon–shaped profile can be defined. Besides, the
barycenter of each profile was determined. This point has
turned out to be very close to the equilibrium position of
the journal center.
The co–ordinates of the journal center have been
evaluated during all the tests by means of two proximity
probes. Then, the values of eccentricity B Je O O ,
attitude angle ( , which is the angle between x-axis and
B JO O ) and eccentricity ratio ( ) can be calculated as
(see in Fig. 4):
2 2
equilibrium equilibriume x x y y (3)
1tan [ ]equilibrium
equilibrium
x xrad
y y
(4)
b
e
C (5)
Fig. 4. Test–rig reference system
The method used for the bearing clearance
measurement Cb (see Fig. 5) is described in [11]. The tests
for the clearance measurement are performed after those
used to define the clearance profile.
Fig. 5. Titling pad bearing clearance measurement
Y
Xe
ø (+)
Non-driven view
OB
OJ
X
Pad 1
Pad 3Pad 4
shaft
Test
condition
#1 #2 #3 #4
10Hz 25Hz 40Hz W = 3.535kN
1 Clearance profile
(Test A1)
Clearance profile
(Test A2)
Clearance profile
(Test A3)
Clearance profile
(Test A4)
2 Equilibrium
position
Equilibrium
position
Equilibrium
position
Equilibrium
position
3 5 kN 5 kN 5 kN 5 Hz
4 6 kN 6 kN 6 kN 10 Hz
5 4 kN 4 kN 4 kN 15 Hz
6 7 kN 7 kN 7 kN 20 Hz
7 3 kN 3 kN 3 kN 25 Hz
8 8 kN 8 kN 8 kN 30 Hz
9 2 kN 2 kN 2 kN 35 Hz
10 9 kN 9 kN 9 kN 40 Hz
11 1 kN 1 kN 1 kN 45 Hz
12 Bearing
clearance Cb
Bearing
clearance Cb
Bearing
clearance Cb
Bearing
clearance Cb
13 Clearance profile
(Test A2)
Clearance profile
(Test A3)
Clearance profile
(Test A4)
Clearance profile
(Test A5)
Table 2. Operating conditions for measurements on TPJB
As shown in Fig. 5, the shaft is pushed upwards in
between of the two upper pads (pad 3 and pad 4): this is the
highest position of the shaft. Then, the shaft is moved to
the lower pad (pad 1): this is the lowest position of the
shaft. The value of Cb can be calculated using the formula,
based on geometrical considerations, reported in [11]:
0.894bC X (6)
Each series of test consisted of a combination of shaft
rotational speed and bearing loads, corresponding to
different Sommerfeld numbers and eccentricity values.
Before and after each test run, once the rotation had
stopped the clearance profiles of bearing which were
named as test A1 – A5 were defined by rotating force as
mentioned previously (see Table 2). The aim of this
procedure is to see the effect of temperature before and
after each test run to the clearance profile of TPJBs.
After having obtained the clearance profile of bearing,
using interpolation, five points at peaks of the
shaped-pentagon profile can be identified. Besides, the
barycenter of each profile was determined. This point is
very close to the position of equilibrium of the center of the
bearing (see Fig. 6 - Fig. 9).
Four test series were run and each one consisted of
nine different conditions. The tests series #1, #2, and #3
were run at constant rotational frequency, respectively
10 Hz, 25 Hz, and 40 Hz, with measurements taken using
nine bearing loads, from 1 to 9 kN on each bearing, in steps
of 1 kN. Because the oil temperature strongly depended on
the bearing load, the loads were applied on the bearing as
listed in Table 2, for maintaining the temperature in the
aforementioned range. The test series #4 was performed by
applying a constant bearing load, equal to 3.535k N on
each bearing, and by changing the shaft rotational speed
from 5 Hz to 45 Hz, with steps of 5 Hz.
IV. Results and discussions
The bearing eccentricity measurements, shown in Fig.
6 - Fig. 9, are plotted as a function of the rotational speed
and of the applied load, along with the bearing clearance
profiles, before and after each series of tests. The
temperatures of the oil and of the pads during the five tests
are listed in Table 3.
As shown in Fig. 6, when the rotational speed is low,
the measured eccentricity deviates slightly from the
bearing vertical centerline. The largest eccentricity, which
corresponds to the maximum load of 9 kN, is about 70 µm.
The clearance profiles of two tests, namely A1 and A2,
corresponding to different temperatures, are also plotted in
Fig. 6. The equilibrium position and the barycenters of two
pentagon–shaped clearance profiles are either coincident
or very close each other. It can be seen that, when the
temperature of inlet oil increases, then the pentagon shape
tends to shrink. This trend shows a good agreement with
the clearance profile changes reported in [6].
When the rotational speed increases, the deviation of
the measured eccentricity from the vertical centerline
grows (especially at 40 Hz), though the largest
eccentricities decrease with respect to that of the test at
10 Hz. This indicate that the bearing cross–coupling
stiffness coefficients (kxy and kyx) cannot be neglected and
that they have some influence on the dynamic performance
of the bearing under test, at least in these specific operating
conditions. Besides, the distance between the equilibrium
position and the barycenters increases almost
proportionally with the rotational speed.
Fig. 9 shows the eccentricity values for test series #4.
It is evident that the deviations of the measured
eccentricity from the bearing vertical centerline are quite
large, even in correspondence of low rotational speed. This
effect might be caused by the relatively large difference of
the temperature between the pads and the oil. As shown in
Table 3, the temperature difference is about 12°C before
beginning the test (profile A4) and 10°C after ending the
test (profile A5).
Fig. 6. Eccentricity measurement at a constant speed of 10Hz
Fig. 7. Eccentricity measurement at a
constant speed of 25Hz
Fig. 8. Eccentricity measurement at a
constant speed of 40Hz
Fig. 9. Eccentricity measurement at a
constant static load of 3.535kN
The measured eccentricities, as a function of the
applied static loads, are shown in Fig. 10 for three different
rotational speeds. It results that the eccentricity is almost
inversely proportional to the rotational speed and
practically linear to the static load.
Fig. 10. Titling pad bearing clearance measurement
Test Test
A1
Test
A2
Test
A3
Test
A4
Test
A5
Pads [°C] 39.70 43.60 46.00 50.80 47.40
Inlet [°C] 36.60 39.40 38.50 38.35 37.56
Outlet [°C] 39.41 39.27 40.27 41.22 39.64
Table 3. Operating temperatures
The measured eccentricity ratios and attitude angle, as
a function of the Sommerfeld number calculated using
nominal radial clearance and pads’ average temperature,
are shown in Fig. 11 and Fig. 12 and a summary of
measured static bearing eccentricities and the
corresponding fitting curve for the five-pads TPJB is
shown in Fig. 13. These Sommerfeld number are based on
the oil viscosity corresponding to the bearing pad
temperature.
It should be noted from Fig. 11 and Fig. 12 that large
Sommerfeld number; i.e. denoting small load, high speed
or large lubricant viscosity, determine small operating
journal eccentricities (small eccentricity ratios) or nearly
1000 2000 3000 4000 5000 6000 7000 8000 90000
10
20
30
40
50
60
70
Static Load [N]
Eccentr
icity [
m
]
= 10Hz
= 10Hz - Fitted curve
= 25Hz
= 25Hz - Fitted curve
= 40Hz
= 40Hz - Fitted curve
centered operation, 0, 2e (90°). That is, the
journal eccentricity vector is nearly orthogonal to the
applied load. On the other hand, small Sommerfeld
number; i.e. denoting large load, low speed or low
lubricant viscosity, determine large operating journal
eccentricities (large eccentricity ratios), 1, 0e
(0°). Note that the journal eccentricity vector is nearly
parallel to the applied load
Fig. 11. Measured static bearing eccentricities versus Sommerfeld number
for a five-pad TPJB
Fig. 12. Measured attitude angle versus Sommerfeld number for a five-pad TPJB
It is clearly seen that, in Fig. 13 most of experimental
results either touch or coincide with each other when the
Sommerfeld number falls within the range of 0.1 and 0.5.
Fig. 13. A summary of measured static
bearing eccentricities versus Sommerfeld number for the five-pads TPJB
V. Conclusions
The paper presents a procedure, along with its
experimental validation, for the identification of the
eccentricity and the assembled bearing clearance Cb of a
five–pads TPJB with LOP configuration.
The clearance profile of the bearing strongly depends
on the operating temperature and the actual dimensions of
the pads. The measurements also confirmed that the
equilibrium position of journal center is close to the
barycenter of pentagon–shaped clearance when the
rotational speed of the shaft is low.
It is necessary to take into account the cross–coupling
stiffness coefficients (kxy and kyx) when dynamic
characteristics of the test bearing are evaluated, especially
at high speed.
The measured eccentricity is almost inversely
proportional to the rotational speed and practically linear
to the static load applied to the rotor bearing system.
The effects of the preload factor on the eccentricity
will be investigated in the near future.
References
[1] Jones G.J. and Martin F.A., "Geometry Effects in
Tilting-Pad Journal Bearings," ASLE Transactions, vol. 22,
no. 3, pp. 227-244, 1979.
[2] Orcutt F.K. and Arwas E.B., "The Steady State and Dynamic
Characteristics of a Full Circular Bearing and a Partical Arc
Bearing in the Laminar and Turbulent Flow Regimes,"
ASME Journal of Lubritation Technology, vol. 89, pp.
143-152, April 1967.
[3] Tonnesen J. and Hansen P.K., "Some experiments of the
Steady State Characteristics of a Cylindrical Fluid-Film
Bearing Considering Thermal Effects," ASME Journal of
Tribology, vol. 103, no. 1, pp. 107-114, January 1981.
[4] Tripp H. and Murphy B., "Eccentricity Measurements on a
Tilting-Pad Bearing," ASLE Transactions, vol. 28, no. 2, pp.
217-224, 1984.
[5] Walton N.V. and San Andrés L., "Measurements of Static
Loading Versus Eccentricity in a Flexure-Pivot Tilting Pad
Journal Bearing," ASME Journal of Tribology, vol. 119, pp.
297-304, April 1997.
[6] Wilkes J.C. and Childs D.W., "Tilting Pad Journal Bearings -
A Discussion on Stability Calculation, Frequency
Dependence, and Pad and Pivot," ASME Journal of
Engineering for Gas Turbines and Power, vol. 134, no. 12,
pp. 1-17, December 2012.
[7] Chatterton S., Pennacchi P., Dang P.V. and Vania A., "A Test
Rig for Evaluating Tilting–Pad Journal Bearing
Characteristics," Proceedings of the 9th IFToMM
International Conference on Rotor Dynamics, vol. 21, pp.
921-930, 22-25 September 2014. doi:
10.1007/978-3-319-06590-8_75
[8] Chatterton, S., Pennacchi, P., Vania, A., Tanzi, E., and Ricci,
R., "Characterization of Five-Pad Tilting-Pad Journal
Bearings Using an Original Test-Rig," ASME Paper
DETC2011-48166,Washington, DC, USA, vol. 1, pp.
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[9] Chatterton S., Pennacchi P., Dang P.V. and Vania A.,
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Tilting–Pad Journal Bearing," Proceedings of the 9th
IFToMM International Conference on Rotor Dynamics, vol.
21, pp. 931-941, 2014. doi: 10.1007/978-3-319-06590-8_76
[10] Nicolas J.C., Gunter E.J. Jr. and Allaire P.E., "Stiffness and
Damping Coefficients for the Five-Pad Tilting-Pad
Bearing," ASLE Transactions, vol. 22, no. 2, pp. 113-124,
1979.
10-2
10-1
100
101
0
0.1
0.2
0.3
0.4
0.5
Speed = 10Hz
10-2
10-1
100
101
0
0.1
0.2
0.3
0.4
0.5
Speed = 25Hz
10-2
10-1
100
101
0
0.1
0.2
0.3
0.4
0.5
Sommerfeld number [S]
Speed = 40Hz
10-2
10-1
100
101
0
0.1
0.2
0.3
0.4
0.5
Sommerfeld number [S]
Load = 3.535kN
10-2
10-1
100
101
0
20
40
60
80
Ang
le [°]
Speed = 10Hz
10-2
10-1
100
101
0
20
40
60
80
Ang
le [°]
Speed = 25Hz
10-2
10-1
100
101
0
20
40
60
80
Sommerfeld number [S]
Ang
le [°]
Speed = 40Hz
10-2
10-1
100
101
0
20
40
60
80
Sommerfeld number [S]
Ang
le [°]
Load = 3.535kN
10-2
10-1
100
1010
0.05
0.1
0.15
0.2
0.25
0.3
0.35
0.4
0.45
0.5
Sommerfeld number [S]
Eccentr
icity R
atio [
]
Speed = 10Hz
Speed = 25Hz
Speed = 40Hz
Load = 3.535kN
[11] Nicholas J.C., "Tilting Pad Bearing Design," in Proceedings
of the twenty-third turbomachinery symposium, Texas
A&M University, 1994.
[12] Chatterton, S., and Pennacchi, P., and Ricci, R., 2010,
“Application and Comparison of High Breakdown-Point and
Bounded-Influence Estimators to Rotor Balancing”, J. Vib.
Acoust. 132(6), 064502. Doi:10.1115/1.4001842
[13] Pennacchi, P., Chatterton, S., and Ricci, R., 2010, “Rotor
Balancing Using High Breakdown-Point and
Bounded-Influence Estimators”, Mech. Syst. Signal
Process., 24(3), pp. 860-872.
doi:10.1016/j.ymssp.2009.10.004
[14] Pennacchi, P., Vania, A., Chatterton, S., and Pesatori, E.,
2010, “Case History of Pad Fluttering in A Tilting-Pad
Journal Bearing”, ASME Paper No. GT2010-22946, ASME
Turbo Expo: Power for Land, Sea and Air, 6, pp. 227-233.
Doi:10.1115/GT2010-22946
[15] Vania, A., Pennacchi, P., and Chatterton, S., 2012, “Dynamic
Effects Caused by the Non-Linear Behavior of Oil-Film
Journal Bearings in Rotating Machines,” ASME Paper
GT2012-69457, ASME Turbo Expo: Turbine Technical
Conference and Exposition, 7, pp. 657-664.
Doi:10.1115/GT2012-69457
[16] Vania, A., Pennacchi, P., and Chatterton, S., 2012, “Analysis
of the sensitivity to non-linear effects in the oil-film forces of
journal bearings,” Proc. of 10th IMECHE International
Conference on Vibrations in Rotating Machinery, London,
UK, C1326-037
[17] Vania, A., Pennacchi, P., Chatterton, S., and Tanzi, E., 2013,
“Sensitivity Analysis of Non-Linear Forces in Oil-Film
Journal Bearings”, World Tribology Congress 2013, Torino,
Italy, pp. 1-4.
[18] Bachschmid N., Pennacchi, P., Chatterton, S., and Ricci, R.,
2009, “On Model Updating of Turbo-Generator Sets”,
Journal of Vibroengineering, 3(11), pp. 379-391
[19] P., Borghesani, P., Ricci, R., Chatterton, S., and Pennacchi,
P., 2013, "A new procedure for using envelope analysis for
rolling element bearing diagnostics in variable operating
conditions", Mechanical Systems and Signal Processing,
38(1), pp. 23-35. doi:10.1016/j.ymssp.2012.09.014
[20] Pennacchi, P., Borghesani, P., Chatterton, S., and Vania, A.,
2012, "Hydraulic Instability Onset Detection in Kaplan
Turbines by Monitoring Shaft Vibrations", ASME Paper No.
DETC2012-70963, pp. 715-722,
doi:10.1115/DETC2012-70963
[21] Chatterton, S., and Pennacchi, P., and Ricci, R., 2010,
“Application and Comparison of High Breakdown-Point and
Bounded-Influence Estimators to Rotor Balancing”, J. Vib.
Acoust. 132(6), 064502. Doi:10.1115/1.4001842
[22] Pennacchi, P., Chatterton, S., and Ricci, R., 2010, “Rotor
Balancing Using High Breakdown-Point and
Bounded-Influence Estimators”, Mech. Syst. Signal
Process., 24(3), pp. 860-872.
doi:10.1016/j.ymssp.2009.10.004
[23] Pennacchi, P., Vania, A., Chatterton, S., and Pesatori, E.,
2010, “Case History of Pad Fluttering in A Tilting-Pad
Journal Bearing”, ASME Paper No. GT2010-22946, ASME
Turbo Expo: Power for Land, Sea and Air, 6, pp. 227-233.
Doi:10.1115/GT2010-22946
[24] Vania, A., Pennacchi, P., and Chatterton, S., 2012, “Dynamic
Effects Caused by the Non-Linear Behavior of Oil-Film
Journal Bearings in Rotating Machines,” ASME Paper
GT2012-69457, ASME Turbo Expo: Turbine Technical
Conference and Exposition, 7, pp. 657-664.
Doi:10.1115/GT2012-69457
[25] Vania, A., Pennacchi, P., and Chatterton, S., 2012, “Analysis
of the sensitivity to non-linear effects in the oil-film forces of
journal bearings,” Proc. of 10th IMECHE International
Conference on Vibrations in Rotating Machinery, London,
UK, C1326-037
[26] Vania, A., Pennacchi, P., Chatterton, S., and Tanzi, E., 2013,
“Sensitivity Analysis of Non-Linear Forces in Oil-Film
Journal Bearings”, World Tribology Congress 2013, Torino,
Italy, pp. 1-4.
[27] Bachschmid N., Pennacchi, P., Chatterton, S., and Ricci, R.,
2009, “On Model Updating of Turbo-Generator Sets”,
Journal of Vibroengineering, 3(11), pp. 379-391
[28] P., Borghesani, P., Ricci, R., Chatterton, S., and Pennacchi,
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