This material is supported by the TAMU Turbomachinery Research Consortium. Parts of the investigation were conducted under NASA NRA on Subsonic Rotary Wing, SSRW2-1.3 Oil-Free Engine Technology (Foil Gas Bearing Modeling). Grant Cooperative Agreement NNX07P98A. Luis San Andrés Luis San Andrés Mast-Childs Professor Fellow ASME Texas A&M University Keun Ryu Keun Ryu Sr. Development Engineer BorgWarner Turbo Systems ASME Turbo Expo 2011: Power for Land, Sea and Air June 6-10, 2011, Vancouver, BC GT2011-45763 On the Nonlinear Dynamics of Rotor-Foil Bearing Systems: Effects of Shaft Acceleration, Mass Imbalance and Bearing Mechanical Energy Dissipation Presentation available at http://rotorlab.tamu.edu
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This material is supported by the TAMU Turbomachinery Research Consortium. Parts of the investigation were conducted under NASA NRA on Subsonic Rotary.
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This material is supported by the TAMU Turbomachinery Research Consortium. Parts of the investigation were conducted under NASA NRA on Subsonic Rotary Wing, SSRW2-1.3 Oil-Free Engine Technology (Foil Gas Bearing Modeling). Grant Cooperative Agreement NNX07P98A.
Luis San AndrésLuis San AndrésMast-Childs Professor
Fellow ASMETexas A&M University
Keun RyuKeun RyuSr. Development Engineer
BorgWarner Turbo Systems
ASME Turbo Expo 2011: Power for Land, Sea and Air June 6-10, 2011, Vancouver, BC
GT2011-45763
On the Nonlinear Dynamics of Rotor-Foil Bearing Systems:
Effects of Shaft Acceleration, Mass Imbalance and Bearing Mechanical Energy
Dissipation
Presentation available at http://rotorlab.tamu.edu
Series of corrugated foil structures (bumps) assembled within a bearing sleeve.
Integrate a hydrodynamic gas film in series with one or more structural layers.
Applications: ACMs, micro gas turbines, turbo expanders, blowers, etc
Reliable with adequate load capacity and high temperature capability
Tolerant to misalignment and debris Need coatings to reduce friction at start-up
& shutdown Damping from dry-friction and operation
with limit cycles
Gas Foil Bearings – Bump type
OIL-FREE Systems! reduce overall system weight, complexity, and maintenance cost increase system efficiency due to low power losses extend maintenance intervals.
Gas Foil Bearings Issues
Endurance: performance at start up & shut down
Little test data for rotordynamic force coefficients
Thermal management for high temperature applications (gas turbines, turbochargers)
Prone to subsynchronous whirl and limit cycle operation – Forced nonlinearity!
NOT rotordynamic instability (San Andrés, 2007)
AIAA2007-5094
San Andrés, L. and Kim, T. H., 2008, “Forced Nonlinear Response of Gas Foil
Bearing Supported Rotors,” Tribol. Int., 41(8)
TAMU research on foil bearingsyear Topic
2008-11 Metal Mesh Foil Bearings: construction, verification of lift off performance and load capacity, identification of structural stiffness and damping coefficients, identification of rotordynamic force coefficients
2008-10 Extend nonlinear rotordynamic analysisPerformance at high temperatures, temperature and rotordynamic measurements
2007-09 Thermoelastohydrodynamic model for prediction of GFB static and dynamic forced performance at high temperatures
2005-07 Integration of Finite Element structure model for prediction of GFB static and dynamic forced performance
Effect of feed pressure and preload (shims) on stability of FBS. Measurements of rotordynamic response.
2005-07 Rotordynamic measurements: instability vs. forced nonlinearity?
2005-06 Model for ultimate load capacity, Isothermal model for prediction of GFB static and dynamic forced performance
2004-09 Measurement of static load capacity, Identification of structural stiffness and damping coefficients. Ambient and high temperatures
Overview – Subsynchronous motions
Heshmat (2000): Operation of a flexible rotor-GFB system at super critical bending mode rotor speeds. Large amplitude subsynchronous motions suddenly appear while crossing system bending critical speed.
Heshmat (1994): GFB operates at max speed of 132 krpm, i.e. 4.61 ×106 DN, showing stable limit cycle operation with large amplitude subsynchronous motions at frequency = rigid body mode natural frequency .
Lee, et al. (2004, 2003): GFBs with viscoelastic layer eliminate large subsynchronous whirl motions appearing in flexible rotor-GFB system (2004) and a two stage centrifugal compressor (2003).
San Andrés et al. (2006): Small imbalances lead to mainly synchronous rotor motions. Large mass imbalances cause sub harmonic motions at rotor speeds > 2 x system natural frequency (whirl frequency ratio ~ 50%) => nonlinear forced rotor responses
San Andrés et al. (2007): Introduce simple GFB model as a nonlinear structure. rotor-GFB performs as a Duffing oscillator with multiple frequency response. Agreement between predictions and test data. 1/2 and 1/3 WFRs due to nonlinearity. (First paper predicting NL forced response of rotor-GFB systems with validations to reliable test data)
Example 1 – Subsynchronous motions
Heshmat (1994)- Maximum speed 132 krpm, i.e. 4.61 ×106 DN.- Stable limit cycle operation with large amplitude sub harmonic motions at whirl frequency = rigid body mode natural frequency .
Subsynchronous amplitude at 350 Hz
Synchronous, 2,200 Hz (132 krpm)
Supersynchronous amplitude at 3,300 Hz (bending mode)
Subsynchronous amplitude recorded during rotor speed
coastdown from 132 krpm (2,200 Hz)
Whirl amplitude remains ~ constant as subsynchronous frequency drops from 350 Hz to 180 Hz
Heshmat (1994)- Maximum speed 132 krpm, i.e. 4.61 ×106 DN.- Stable limit cycle operation but with large amplitude subsynchronous motions. Whirl frequency tracks rotor speed
Example 1 – Subsynchronous motions
Heshmat (2000) Flexible rotor- GFB system operation to 85 krpm (1.4 kHz): 1st bending critical speed:34 krpm (560 Hz)
Waterfall plot recorded during rotor speed coastdown test from 45 krpm (750 Hz)
Rotor orbit shape at 45k rpm
Large amplitude limit cycle motions above bending critical speed, whirl frequency = natural frequency (rigid body)
Example 2 – Subsynchronous motions
Lee, et al. (2003, 2004)Flexible rotor supported on GFBs with viscoelastic layer
Viscoelastic layer eliminates large motions at natural frequency & appearing above 1st bending critical speed.
50 kRPM (833 Hz)
Bump type GFBViscoelastic GFB
Synchronous vibration
1st bending mode
Rigid body mode
Bum
p ty
pe G
FB
Vis
coel
astic
GF
BSynchronous
vibration
Example 3 – Subsynchronous motions
0 200 400 600 800 1000 1200 1400 1600 1800 20000
5
10
15
20
25
30
35
40Waterfall -Horizontal
Frequency [Hz]
Am
plitu
de
.
.Frequency [Hz]
Dis
pla
cem
ent
[um
]
1 X
Whirl and bifurcation at high rotor speeds
Ro
tor
coas
tin
g d
ow
n
Max. Rotor speed = 69 krpm
San Andrés, L., et al., 2011, “Identification of Rotordynamic Force Coefficients of a Metal Mesh Foil Bearing Using Impact Load Excitations,” ASME J. Eng. Gas Turbines Power, Vol. 133
Example 4 – Subsynchronous motions
Metal Mesh Foil Bearing
RudDloff, L., Arghir, M., et al., 2011, “Experimental Analysis of a First generation foil Bearing. Start-Up Torque and Dynamic
Coefficients,” ASME GT2010-22966
Example 5 – Subsynchronous motions
Unloaded FB: “Self-Excited” whirl motions at speed 30 krpm (500 Hz) with whirl frequency=165 Hz (WFR=0.33)
Kim, D., Shetty P., Lee. D., 2011, “Imbalance Response of a Rotor Supported
by Hybrid Air Foil Bearings,” ASME GT2011-45576
Example 6a – Subsynchronous motions
Loaded hybrid FB (vertical): 2.67 bar gauge supply pressure Sub sync whirl motions start at 20 krpm with (nat) freq 5900 rpm (WFR=0.30). Too large amplitudes at 30 krpm, test stopped
Kim, D., Shetty P., Lee. D., 2011, “Imbalance Response of a Rotor Supported
by Hybrid Air Foil Bearings,” ASME GT2011-45576
Example 6b – Subsynchronous motions
Loaded hybrid FB (vertical): 4 bar gauge supply pressure Large amplitude whirl motions start at 34 krpm (567 Hz) with whirl frequency~natural frequency 7200 rpm (WFR=0.21)
Amplitudes of subsynchronous
motions INCREASE as
imbalance increases (forced
nonlinearity!)
last two indices are multipliers for X & Y axis offset
0 100 200 300 400 500 600 700 8000
20
40
60
80
100
Frequency [Hz]
Am
plit
ud
e [
mic
ron
s]
last two indices are multipliers for X & Y axis offset
0 100 200 300 400 500 600 700 8000
20
40
60
80
100
Frequency [Hz]
Am
plit
ud
e [
mic
ron
s]D
ispl
acem
ent
Am
plitu
de
(μm
) D
ispl
acem
ent
Am
plitu
de
(μm
)
Frequency (Hz)
25.7 krpm
2.6 krpm u = 7.4 μm
1X 0.5X
2X
1X 0.5X
2X
8.5 krpm
25.7 krpm
2.6 krpm
12.5 krpm
20.5 krpm
u = 10.5 μm
Frequency (Hz)
Rotor speed +
Imbalance +
San Andrés, L., Rubio, D., and Kim, T.H, 2007, “Rotordynamic Performance of a Rotor
Supported on Bump Type Foil Gas Bearings: Experiments and Predictions,” ASME J. Eng.
Gas Turbines Power, 129
Example 7 – Subsynchronous motions
Gen II foil bearings
2 krpm
25 krpm
50 krpm-400 -200 0 200 400 600 800 1000
Frequency [Hz] 1X
100
80
60
40
20
0
Am
pli
tud
e [µ
m]
Large amplitudes locked at natural frequency (50
krpm to 27 krpm) ……
but stable limit cycle!
Kim, T.H., and San Andrés, L., 2009, “Effects of a Mechanical Preload on the Dynamic Force Response of
Gas Foil Bearings - Measurements and Model Predictions,” STLE Tribol. Trans., 52
Rotor speeddecrea
ses
Example 7 – Subsynchronous motions
Gen II foil bearings
Analysis vs. test data
0 100 200 300 400 500 6000
20
40
60
80
PredictionExperiment
Frequency [Hz]
Am
plitu
de [
um]
0 5 10 15 20 25 300
40
80
120
160
200
PredictionExperiment
Rotor speed [krpm]
Fre
quen
cy [
Hz]
(a) Subsynchronous Amplitude vs frequency (b) Subsynchronous frequency vs speed
Am
plitu
de [
μm]
Subsynchronous whirl frequencies concentrate in a narrow band enclosing natural frequency (132 Hz) of test system
0 100 200 300 400 500 6000
20
40
60
80
PredictionExperiment
Frequency [Hz]
Am
plitu
de [
um]
0 5 10 15 20 25 300
40
80
120
160
200
PredictionExperiment
Rotor speed [krpm]F
requ
ency
[H
z]
(a) Subsynchronous Amplitude vs frequency (b) Subsynchronous frequency vs speed
Amplitude vs. frequency Frequency vs. rotor speed
Test data
Predictions
Test data
Predictions
Rotor speed (krpm)Frequency (Hz)
San Andrés, L. and Kim, T. H., 2008, “Forced Nonlinear Response of Gas Foil Bearing Supported Rotors,” Tribol. Int., 41(8)
AIR SUPPLY
Cooling flow/feed pressure on FB motions
Ps
Rotating journal
Pa
Bump spring
Top foil Bearing housing
Circumferential velocity
ΩRJ Axial
velocity Ω RJ
Outer gap
Inner gas film
X
Y
z x
Typically foil bearings DO not require pressurization.
Cooling flow is for thermal management: to remove
heat from drag or to reduce thermal gradients in hot/cold
engine sections
Side effect: Axial flow retards evolution of circumferential flow velocity
San Andres et al, ASME JGT, 209, v31
Effect of side flow on rotordynamics
(a) 0.35 bar
(b) 1.4 bar
(c) 2.8 bar
Whirl frequency locks at RBS
natural frequency ( not
affected by level of feed pressure
For Ps ≥ 2.8 bar rotor subsync. whirl motions
disappear;(stable rotor
response)
ωsub= 132 Hz
ωsub= 147 Hz
ωsub= 127 Hz
Subsynchronous ωsyn= 508 Hz
Synchronous
FFT of shaft motions at 30 krpm
San Andres et al, ASME JGT, 209, v31
Onset of subsynchronous whirl motions
(a) 0.35 bar
(b) 1.4 bar
(c) 2.8 bar
SynchronousSubsynchronous
NOS: 25 krpm
NOS: 30.5 krpm
NOS: 27 krpm
Delay of large
amplitude subsynchro
nous rotor motions
with increase in
axial cooling flow
(feed pressure)
Effect of side flow on rotordynamics
San Andres et al, ASME JGT, 209, v31
Objectives
To extend earlier analysis to predict the forced response of a rigid rotor supported on FBs modeled as nonlinear structure with material damping.To determine the effects of rotor acceleration, imbalance mass, and the FB structural loss factor on the dynamic forcedresponse of simple RBS.
Most GFB analyses are complex; coupling top foil & under spring models with gas film flow model.
butGFB forced performance depends mainly on the material properties of the support elastic structure
Dynamic Stiffness & Damping Mechanism for Foil Bearing
Dynamic Stiffness & Damping Mechanism for Foil Bearing
GT2011-45763
Fast accelerations are typical in MTM due to small rotor mass moment of inertia. This work provides design and operation considerations for the appropriate selection and use of GFBs to avoid the build up of excessive nonlinear RBS response.
FB load–deflection structural test
Nonlinear bearing forced deflection. Hysteresis loop shows energy dissipation
Loading
Loading
Unloading
Unloading
Stiffness hardening is
likely to induce internal
resonances at rotor speeds
greater than the RBS natural
frequency
Kim and San Andrés (2007): Eight cyclic load - unload
structural tests on Gen II foil bearing
Load–Deflection Structural tests
Nonlinear bearing forced deflection: test data, polynomial fit & model prediction
F = r (0.0675 -0.002 r + 0.0001 r2 )
Test data
Prediction
2 31 2 3sFBF K r K r K r
Kim and San Andrés (2007): Eight cyclic load - unload
structural tests on Gen II foil bearing
r
FFB
FB load–deflection structural test
FB Structural Loss Factor
0 20 40 60 80 100
0
0.05
0.1
0.15
0.2
FB deflection [um]
Str
uctu
ral l
oss
fact
or [
-]
*
FB deflection [μm]
Loss factor (γ) represents structural damping and is obtained from load-deflection hysteresis loop
TYP, loss factor is large at small displacements BUT decreases for large displacements. Typical of structural system with dry-friction
2
1FBs
S
F drK r
where
sBS
FK r
local stiffness coefficient
r
21 2 32 2 31
2
E E
n
K K x K xf
M
Natural frequency for small amplitude motions about SEP:
Notable differences in the onset speed and persistence of whirl motions show the RBS has a marked mechanical hysteresis
Ramp rate
31
Whirl frequencies: +α
α= +35 Hz/s (SLOW acceleration)
u=8 µm. FB γ=0.14
WFR=ω/Ω
Subsynchronous whirl motions from 11 to 20 krpm with WFR=½ at first, and later from 20 to 36 krpm jump to WFR=⅓. Above 28 krpm, more complex WFRs ranging from 0.31 to 0.37, slightly above and below ⅓.
00.10.20.30.40.50.60.70.80.9
1
0 10 20 30 40
Rotor speed [krpm]
WF
R
2 × f n 3 × f n1 × f n
Once a subsynchronous frequency motion appears, its
amplitude rapidly increases with rotor speed.
Significant motion amplitudes
with WFR=½ and WFR=⅓ appear at ~twice and ~three times the
system natural frequency.
0
20
40
60
80
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
1 × fn
3 × fn
2 × f n 3 × f n1 × f n
32
Whirl frequencies: -α
α= -35 Hz/s (SLOW deceleration)
u=8 µm. FB γ=0.14
WFR=ω/Ω
For rotor speeds > ~20 krpm (333 Hz), motions with WFRs ranging from 0.27 to 0.41, i.e., a chaotic regime, are apparent.
00.10.20.30.40.50.60.70.80.9
1
0 10 20 30 40
Rotor speed [krpm]
WF
R
2 × f n 3 × f n1 × f n
0
20
40
60
80
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
2 × f n 3 × f n1 × f n
The motions with a 50% WFR are not as severe in
amplitude as when the rotor accelerates,
occurring over a shorter rotor speed span.
33
Effect of rotor acceleration u=8 µm. FB γ=0.14
0
10
20
30
40
50
60
0 10 20 30 40
Rotor speed [krpm]
Am
plitu
de [
µm
]
Acceleration
Deceleration
Linear response
Acceleration
Linear response
Deceleration
Natural frequency (f n )
The peak amplitude during rotor deceleration is ~10 µm smaller than the one predicted during rotor acceleration
xL =u/γ = 8 µm/0.14 = 57.1 µm
Synchronous response ± 71 Hz/s
2
22 2
( ')
1 ( ') ( ')L
rx u
r r
'n
fr
f
Linearized model
=7800 rpm
Effect of mass imbalance on RBS forced response
35
Effect of rotor mass imbalance α= +283 Hz/s, FB γ=0.14
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
sp
ee
d [
krp
m]
2
13
2
4
35
1X
1 × fn
2 × fn
3 × fn
Vertical response (x)
½WFR½ WFR3½ WFR3
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
spee
d [
krp
m]
2
1
3
24
3
5
1X
1 × fn
2 × fn
3 × fn
Vertical response (x)
½WFR½ WFR3½ WFR3
0
20
40
60
80
100
120
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
2 × f n 3 × f n1 × f n
0
20
40
60
80
100
120
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
2 × f n 3 × f n1 × f n
u=4 μm u=20 μm
Imbalance
Mass imbalance exacerbates the bearings’ nonlinearity and showcases a distinctive jump phenomenon
36
Effect of rotor mass imbalance u=20 µm. FB γ=0.14
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
spee
d [
krp
m]
2
1
3
24
3
5
1X
1 × fn
2 × fn
3 × fn
Vertical response (x)
½WFR½ WFR3½ WFR3
0
20
40
60
80
100
120
140
160
0 5 10 15 20 25 30 35 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
AccelerationDecelerationLinear response
Linear response Acceleration
Deceleration
Natural frequency (f n )
Jump
WFM_YWFM_X
3 × fn
2 × fn
1 × fn
1X
Vertical response (x)
Frequency [Hz]
0 200 400 600 800
Ro
tor
spee
d [
krp
m]
36
2
4
1
3
2
½WFR½ WFR3½ WFR3
α= -283 Hz/s
α= +283 Hz/s
Synchronous amplitude shows stiffness hardening effect with jump phenomenon while rotor accelerates
Synchronous response
37
Whirl frequencies: Imbalance ↑
u= 20 µm α= +283 Hz/s, FB γ=0.14
WFR=ω/Ω
As imbalance mass increases, and for rotor speeds above (3×fn), the rotor motion has a broader whirl motions at ⅓ WFR.
½ frequency whirl disappears for u>20 µm!
00.10.20.30.40.50.60.70.80.9
1
0 10 20 30 40
Rotor speed [krpm]
WF
R
2 × f n 3 × f n1 × f n
0
20
40
60
80
100
120
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
2 × f n 3 × f n1 × f n
Effect of FB loss factor (material damping) on RBS forced response
39
Effect of FB loss factor
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
spee
d [
krp
m]
2
1
3
24
35 1X½WRF½ WFR3½ WFR3
1 × fn
2 × fn
3 × fn
Vertical response (x)WFM_Y
WFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
sp
ee
d [
krp
m]
2
13
2
4
35
1X
1 × fn
2 × fn
3 × fn
½WRF½ WFR3½ WFR3
Vertical response (x)
0
20
40
60
80
100
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR ~1/3WFR
2 × f n 3 × f n1 × f n
0
20
40
60
80
100
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR
2 × f n 3 × f n1 × f n
γ=0.07 γ=0.28
α= +283 Hz/s. FB u=8 µm
Bearing loss factor affects the onset and persistence of rotor sub harmonic motions
FB loss factor
Whirl frequency: FB loss factor ↑
WFR=ω/Ω
½WFR motions are apparent from 8 ~ 15 krpm (1×fn ~ 2× fn)
For γ>0.2, ⅓WFR frequency
components disappear!
γ=0.28 α= +283 Hz/s. u=8 µm
00.10.20.30.40.50.60.70.80.9
1
0 10 20 30 40
Rotor speed [krpm]
WF
R
2 × f n 3 × f n1 × f n
0
20
40
60
80
100
0 10 20 30 40
Rotor speed [krpm]
Am
pli
tud
e [
µm
]
1X ~1/2WFR
2 × f n 3 × f n1 × f n
41
Effect of FB loss factor
0
20
40
60
80
100
120
0 5 10 15 20 25 30 35 40
Rotor speed [krpm]
Am
plit
ud
e [µ
m]
AccelerationDecelerationLinear response
Linear response
Acceleration
Deceleration
Natural frequency (f n )
Jump
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
sp
eed
[k
rpm
]3
6
2
4
13
2
3 × fn
2 × fn
1 × fn
1X
Vertical response (x)
½WFR½ WFR3½ WFR3
WFM_YWFM_X
Frequency [Hz]
0 200 400 600 800
Ro
tor
sp
ee
d [
krp
m]
2
13
2
4
35
1X½WRF½ WFR3½ WFR3
1 × fn
2 × fn
3 × fn
Vertical response (x)
u=8 µm. γ=0.07
α= -283 Hz/s
α= +283 Hz/s
As rotor accelerates, the FB hardening stiffness with little damping ( low) affects more the response (multi-frequency). On deceleration, the rotor synchronous response appears free of nonlinearities
Synchronous response
42
Other NL response: small u & γ
u=1 µm. γ=0.015
For speeds above RBS natural frequency (fn =130 Hz), whirl motions of
large amplitudes with whirl frequency locked at the natural frequency!
α=+283 Hz/s
0 200 400 600 8000
8
16
24
32
40
Frequency [Hz]
Am
plitu
de [
um]
Am
plit
ud
e [
μm
]
Frequency [Hz]2 krpm
35 krpm1X
System natural frequency (fn =130 Hz)
Bearing with little damping! (poor mechanical energy
dissipation)
2 krpm
25 krpm
50 krpm-400 -200 0 200 400 600 800 1000
Frequency [Hz] 1X
100
80
60
40
20
0
Am
pli
tud
e [µ
m]
Example TEST DATA(not same FBs)
ConclusionsFor operation above the RBS system critical speed and as the rotor accelerates, large amplitude whirl motions appear with a main subsynchronous frequency tracking rotor speed, first at 50% speed and later bifurcating into at 33% whirl frequency.
Large rotor imbalances produce both jump phenomenon and a stronger hysteresis during slow acceleration and deceleration cases.
Slow rotor accelerations result in responses with more abundant subsynchronous whirl patterns, increased amplitudes of whirl, and accompanied by a pronounced mechanical hysteresis when the rotor decelerates.
Material damping (dry friction) in the FB aids to reduce and delay the nonlinear response, eventually eliminating the multiple frequency behavior.
GT2011-45763
Recommendation GT2011-45763
Fast rotor start up and coast down procedures Reductions in rotor inertia or larger drive torque
To ameliorate subsynchronous rotor motions resulting from nonlinear effect of hardening support structure
Minimize rotor imbalance (a forcing function) Well-balanced rotor is a must!
Large FB material damping Improvements in GFB design and materials
AcknowledgmentsThanks support of• TAMU TRC (2004-2008)• NASA GRC (2007-09) & Dr. Samuel Howard • NSF (2003-06),• Foster-Miller (FBs)