Gas Turbines: Structures and Dynamics

Dry-Friction Whip and Whirl Predictions for a Rotor-Stator Model With Rubbing Contact at Two Locations

[+] Author and Article Information
Dara W. Childs

 Turbomachinery Laboratory, Texas A&M University, College Station, TX 77843dchilds@tamu.edu

Dhruv Kumar

 Graduate Research Assistant, Texas A&M University, College Station, TX 77845logic87@neo.tamu.edu

J. Eng. Gas Turbines Power 134(7), 072502 (May 23, 2012) (11 pages) doi:10.1115/1.4005979 History: Received August 26, 2011; Revised September 19, 2011; Published May 23, 2012; Online May 23, 2012

The present work investigates dry-friction whip and whirl phenomena for a rigid rotor contacting at two bearing locations. The idea originated with a paper by Clark (2009, “Investigation of the NRG #40 Anemometer Slowdown,” American Wind Energy Association, Windpower 2009, Chicago, IL, pp. 1-16) on an anemometer undergoing dry-friction whip and whirl. The anemometer rotor was supported by two Teflon® bushings within an elastically supported housing. The dry-friction forces arose at the bushings. Prior models for dry friction whirl and whip have considered rub at one nonsupport location. The present analytical model consists of a rigid rotor connected to a rigid stator at two rubbing-contact locations. Analytical solutions are developed for the following normal reaction forces at the contact locations: (1) In phase, and (2) 180° out of phase. Analytical solutions are only possible for the same radius-to-clearance ratio (RCl) at the two rub locations and define regions where dry-friction whirl is possible in addition to indicating possible boundaries between whirl and whip. These solutions are similar to Black’s (1968, “Interaction of a Whirling Rotor with a Vibrating Stator Across a Clearance Annulus,” J. Mech. Eng. Sci., 10 (1), pp. 1-12) and Crandall’s (1990, “From Whirl to Whip in Rotordynamics,” IFToMM Third Intl. Conf. on Rotordynamics, Lyon, France, pp. 19-26). A flexible-rotor/flexible-stator model with nonlinear connections at the bearings was developed to more correctly establish the range of possible solutions. The nonlinear connections at the rub surface are modeled using Hunt and Crossley’s 1975 contact model with Coulomb friction (Hunt and Crossley, F., 1975, “Coefficient of Restitution Interpreted as Damping in Vibroimpact,” ASME J. Appl. Mech., 42 , pp. 440). Dry friction simulations are performed for the following rotor center of gravity (C.G.) configurations with respect to the contact locations: (1) Centered, (2) [3/4]-span location, and (3) overhung, outside the contacts. Predictions from the in-phase analytical solutions and the nonlinear simulations agree to some extent when the rotor mass is centered and at the [3/4]-span location due to the fact that whirl-to-whip transitions occur near the pinned rotor-stator bounce frequency. For the overhung mass case, the nonlinear simulation predicts whip at different frequencies for the two contact locations. Neither analytical solution modes predicts this outcome. No 180 deg out-of-phase solutions could be obtained via time-transient simulations. Dry-friction whirling is normally characterized as supersynchronous precession with a precession frequency equal to the running speed ω times RCl. Simulation predictions for models with different RCl ratio mimic whirling. Specifically, with increasing rotor speed, the backward precessional (BP) frequency increases at each contact location. However, individual contact velocities show slipping at all conditions. Slipping is greater at one location than the other, netting a “whirl-like” motion. For the overhung model with different RCl ratios: in addition to whipping at different frequencies the two contacts also whirl at different frequencies corresponding to the separate RCl ratios at the respective contacts. Simulations predict a different running speed for the “jump up” in precession frequency associated with a transition from whirl-to-whip with increasing running speed than for the jump-down in precession frequency for whirl-to-whip in a speed-decreasing mode.

Copyright © 2012 by American Society of Mechanical Engineers
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Figure 1

Anemometer with spirograph motion (see Clark [12])

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Figure 2

(a) Rotor in X-Z plane, and (b) transverse plane through rotor mass center

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Figure 3

Section view rotor and stator assembly positions

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Figure 4

Stator coordinates showing support connections in the X-Z plane

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Figure 5

Clearance diagram (constraints)

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Figure 6

Mass locations considered

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Figure 7

Mode 1; RClL = RClR, disk at center

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Figure 8

Disk at [3/4] location, RClL = RClR; Mode 1

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Figure 9

(a) Left-contact predictions, disk at center, RClL = RClR = 100, (b) disk at center, RClL = RClR = 100; left, BP versus ω, and (c) disk at center, RClL = RClR = 100; VtL and VtR versus ω for ω increasing

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Figure 10

(a) Disk at [3/4] location; RClL = 100, RClR = 125, BP predictions for left contact. (b) Disk at [3/4] location; RClL = 100, RClR = 125, and VtL and VtR versus ω for increasing ω.

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Figure 11

(a) Overhung disk; RClL = RClR = 100, BPs versus ω for increasing ω. (b) Overhung disk; RClL = RClR = 100; BPs versus ω for decreasing ω.

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Figure 12

Overhung disk; RClL = 100, RClR = 125; BPs versus ω for increasing ω




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