SIngle Blade Broken _ Talcher
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turbine, and the diametral modes number (nD), see
[3] and [4]. In the high cycle fatigue failureanalysis, the vibratory stress due to the flow-
induced vibrations on the bladed disk is determined
in order to compare with the fatigue limit of the
material, [5], [6] and [7]. In this paper, oneproposes a numerical/experimental procedure to
analyse the low cycle fatigue problem.The computational mechanics procedure used
in this work consisted first in digitize a single blade
for obtaining a file with the geometric dimensions
and, secondly, to build a solid CAD model of the
blade. The CAD model was verified by comparingthe calculated and measured blade weights. This
model was analyzed using a finite element code in
order to obtain the natural frequencies and the
associated vibration modes of a single blade in a
free-free condition. A modal testing was also
performed and a numerical/experimentalcomparison was used to adjust the material
properties and the geometric dimensions.
In addition, a five blades grouped was
modeled considering the tie-wire and the shroudas
the elements used to connect the blades. In thiscase, another modal testing was performed and the
numerical/experimental comparison was made to
adjust the material properties introduced in the
computational model with the objective of
simulating the contact between the blade and the
tie-wire and the blades and the shroud. As shownin
several papers and reports, these elements can playa very important role in this type of analysis, [8]. A
combination of modal testing and finite element
analysis are the current procedure to accurately
predict the dynamic response of bladed disks in
turbo-machinery.
Finally, a fifth stage of the low-pressure
turbine model was built to solve the
eigenvalues/eigenvectors problem and the low
fatigue problem was investigated.
II. Modal analysis on a single blade
The purpose of this analysis is to adjust the
material properties and the geometric dimensions of
the blade in the numerical model, in order to fit the
modal testing measurements.
Figure 3 shows the blade configuration for the
modal testing in a free-free condition. The
instruments used for this purpose were a force
transducer B&K 8200, a shock hammer (coupled to
the force transducer), an accelerometer B&K 4344
and the LMS SCADAS III with a Fourier analysis
software. For the mode identification, accelerationswere obtained at 105 points on the blade.
Fig. 3. Experimental set for the modal analysis of a single
blade in a free-free condition
Figure 4 shows the first mode of vibration and
figure 5 shows the second mode of vibration of the
single blade in a free-free condition. In the
numerical model the medium size of the elements is
10 mm and the total number of elements is 14 313.
(a)
(b)
Fig. 4. First mode of the single blade: (a) numerical and
(b) experimental
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(a)
(b)Fig. 5. Second mode of the single blade: (a) numerical
and (b) experimental
TABLE I presents the numerical/experimental
results of the first seven modes of the modal
analysis of a single blade in a free-free condition.
Mode Numerical
(Hz)
Experimental
(Hz)
Error
(%)
1 162,8 166,9 -2,5
2 442,3 451,7 -2,8
3 524,6 547,2 -4,1
4 738,7 748,9 -1,4
5 1.112,0 1.077,2 3,2
6 1.212,0 1.166,1 3,9
7 1.448,0 1.457,7 -0,7
TABLE I Numerical/experimental results on a
single blade
III. Modal analysis on a five blades grouped
A tie-wire and a shroud, as seen in figure 6,
connect groups of four and five blades. The contact
problem between the blade and the tie-wire and the
blade and the shroud is analyzed by using a soft
material between them. So, the purpose of thisanalysis is to adjust the material properties,
introduced in these regions in the numerical model,
so that the numerical solution fits the experimental
results.
Fig. 6. Four and five bladed groups
The experimental set for the modal testing of a
five blades grouped is presented in figure 7. The
instruments used for this purpose were the same
used in the experimental setup in the modal testing
of the single blade test.
Fig. 7. Experimental set for the modal analysis of a five
blades grouped in a clamped-free condition
Figure 8 shows the first mode of the 5 blades
grouped in bending and figure 9 presents the
second mode of the 5 blades grouped in bending. In
the numerical model the medium size of the
elements is 7 mm on the blades, 4 mm on the
shroud, 3 mm on the tie-wire and 2 mm on the
material interface. The total number of elements
used in the model is 98 184.
shroud
tie-wire
root
bladeblade
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Fig. 8. First mode of the five blades grouped in bending
Fig. 9. Second mode of the five blades grouped inbending
TABLE II presents the numerical/experimental
results of the first eight modes of the modal
analysis of a five blades grouped, in a clamped-freecondition. Mode types are bending (B) and/or
torsion (T).
Numerical Experimental
Freq. (hz) Mode Freq. (hz) Mode Mode type
107,8 1 99,4 1 B
- - 142,3 2 B/T
172,7 2 148,5 3 B/T
213,6 3 210,7 4 B/T
- - 296,2 5 B/T
395,2 4 336,4 6 B/T
411,0 5 407,6 7 B/T
499,1 6 479,4 8 B/T
TABLE II. Numerical/experimental results on a fiveblades grouped
IV. Modal analysis of the fifth stage
The fifth stage of the low pressure turbine was
modeled in accordance with the results obtained in
the modal analysis on a single blade and on a fiveblades grouped. It is composed by 133 blades
divided in groups of four and five blades as shown
in figure 10 (five blades group in gray and four
blades group in black).
Fig. 10. Fifth stage model of the low pressure turbine
As found by Chyou in [3], one observes two
modal groups with a large modal density. In the
first modal group, blades are associated with first
mode of the blades grouped in bending (see figure8) and in the second modal group, blades are
associated with the second mode of the blades
group in bending (see figure 9).
TABLE III presents the first diametral modes
in the first group and TABLE IV presents the firstdiametral modes in the second group of the fifth
stage of the turbine turning at its operation speed of
3600 rpm.
The circunferencial modes are not excited by
the force acting on the blades due to steam flow, so
they are ignored in this analysis.
#1 1D 152,70 hz #2 1D 152,8 hz
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#3 2D 153,2 hz #4 2D 153,3 hz
#6 3D 154,1 hz #7 3D 154,4 hz
TABLE III. Diametral modes in the first modal group
#31 1D 184,4 hz #32 1D 184,4 hz
#33 2D 185,1 hz #34 2D 185,4 hz
#35 3D 185,9 hz #36 3D 186,2 hz
TABLE IV. Diametral modes in the second modal group
TABLE V shows the vibrations modes which
can cause the resonance of the fifth stage of theturbine at 3600 rpm due to the harmonics of the
operation speed and due to the diametral modenumber (nD).
Operation
speed(rpm)
Operation
speed (hz)
Harmonic/
Diametral modenumber (nD)
Frequency
(hz)
3600 60 1 60
3600 60 2 120
3600 60 3 180
TABLE V. Diametral modes in the second modal group
In observation of TABLE III, it is possible to
note that the frequencies in the first mode group are
approximately 150 hz, far from the second and the
third harmonics of the operation speed.
Nevertheless, in TABLE IV, it is observed that the
frequencies in the second mode group are
approximately 180 hz, near the third harmonic of
the operation speed.The two 3D diametral modes in the second
mode group 185,9 hz and 186,2 hz have a
deviation of 3,3% and 3,4% from the third
harmonic of the operation speed of the turbine,respectively. Orsagh and Roemer in [4] recommend
a value of 3% far from one of the harmonics to
assure an operation without resonance. Based on
this results, it is possible to conclude that in the
fifth stage of the low-pressure turbine there will be
no low cycle fatigue problem.
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V. Conclusions
In this work, the low cycle fatigue problem was
investigated on a fifth stage of the low-pressure
turbine in a thermoelectric power plant. Theprocedure for this study consisted initially in the
fitting of the computational model of a single blade
and a five blades grouped with experimental
measurements. Further, a computational model of
the complete fifth stage bladed disk was developed
and a modal analysis was performed. By analyzingthe harmonics of the operation speed and the
diametral modes of the bladed disk, it was
concluded that no resonance had occurred, so the
low cycle fatigue is not the root-cause of the
damage on the blades. This fact indicates that the
high cycle fatigue on the blades in the fifth stage of
the low-pressure turbine must be investigated.
References
[1] Dewey, R. P. and Rieger, N. F., 1985, Survey ofBlade Failures in Turbine-Generator Units.
Proceedings: Steam Turbine Blade Reliability
Seminar and Workshop, ed. By R. G. Brown and J.
F. Quilliam, EPRI CS-4001, pp. 2-61 ~ 2-78.
[2] Ortolano, R. J., 1991, Recent Case Histories in theInspection, Modification, and Repair of Steam
Turbine Blading. Proceedings, International Joint
Power Generation Conference, ASME PWR-Vol.13,
pp. 147-154.[3] Chyou, Y., 2000, Root-Cause Investigation on Blade
Failures in Steam Turbines From an Aspect of
Computational Mechanics. Proceedings of 2000
International Joint Power Generation Conference,
Miami, USA.
[4] Orsagh, R. F. and Roemer, M. J., 1994, Examinationof Successful Modal Analysis Techniques Used for
Bladed-Disk Assemblies. Technical Report, Impact
Technologies, New York.
[5] Fleeter, S., Zhou, C., Houstis, E. and Rice, J., 1998,Fatigue Life Prediction of Turbomachine Blading.
Technical Report, Lawrence Livermore National
Laboratory.
[6] Boven, R. and Lam, T. Management Strategy andTechnical Plan Used to Select, Qualify and Procure a
New 20.9 L-1 Stage Steam Turbine Bucket.
Proceedings of 2000 International Joint Power
Generation Conference, Miami Beach, Florida, July
23-26, 2000.
[7] Rao, J. S., Turbine Blade Life Estimation. AlphaScience International Ltd., 2000.
[8] Shiga, M., Vibration Characteristics of GroupedSteam Turbine Blades. JSME International Journal,
pp. 592-596, Series III, Vol. 32, No.4, 1989.