Sorry to ask again about the natural frequency calculation, since I find there are quite many posts on this topic, but still I have some confusion.
I would like to calculate the natural frequencies and damping ratios for some modes of OC3-Hywind.
Before model linearization, I activated 6 platform DOFs and 4 tower DOFs, set rotor rotation speed and wind speed as 0, disabled incident wave or radiation damping, disabled all control inputs.
After linearization, since there is no rotating states, I used “eianalysis.m” from MBC package to produce natural frequencies and damping ratios. The result is listed below.
I believe there is quite a bit of coupling between the tower-bending modes and the rotor blade fexibility for this model. This coupling will have a small impact on the 1st tower-bending frequencies and a large impact on the 2nd tower-bending natural frequenices. I suspect you’ll be able to match the results to NREL/SR-500-45891 much better if you enable the blade-bending DOFs in FAST. More information is available in the forum topic found here: http://forums.nrel.gov/t/tower-eigenfrequencies-of-nrel-5mw-turbine/517/1.
You are right that the blade flexibility does have big influence on the 2nd order tower bending mode. Besides, I found the drivetrain also has big influence on tower side-side bending modes.
I followed your advice by activating 9 blade DOFs and also the drivetrain DOF in addition to previous setup, and it now agrees well with the following result in report NREL/TP-5000-48191.
One other question. In the results of “eianalysis”, the order of states seems different with that defined in .lin file. For example, in the .lin file, the order of states is “surge, sway, heave, pitch, roll, yaw”, but in the natural frequency matrix “NaturalFrequencies”, the order might become “yaw, heave, sway, surge, roll, pitch”. I am wondering how to identify their correspondence.
Good question. I’m surprised this one hasn’t been asked before.
The tower damping in FAST is specified as a fraction of critical damping for each mode of the isolated tower. The damping is implented as a stiffness-proportional modal damping, mathematically as follows. If the i’th generalized elastic force is given as:
Felastic_i = K_ij*q_j,
where K_ij is the (i,j) element of the generalized elastic stiffness matrix of the isolated tower and q_j is the j’th tower-bending degree-of-freedom (DOF), then the i’th generalized damping force is given by:
Fdamping_i = K_ijbeta_jqdot_j,
where qdot_j is the first time-derivative of q_j and beta_j is the stiffness-proportional constant for the j’th DOF. (Einstein notation is used here.) The stiffness-proportional constant is derived from the modal damping ratio of the j’th tower-bending mode (zeta_j) and the j’th natural frequency of the isolated tower (f_j) as follows:
beta_j = zeta_j/(pi*f_j),
f_j = 1/(2*pi)*SQRT(K_jj/M_jj),
where M_ij is the (i,j) element of the generalized mass matrix of the isolated tower.
A few points of clarification for FAST:
*i and j both go from 1 to 2 for both the fore-aft and side-to-side bending modes.
*zeta_j represents TwrFADmp(j)/100 and TwrSSDmp(j)/100 for the fore-aft and side-to-side bending modes, respectively.
*The generalized elastic stiffness matrix of the tower depends on the specified distributed tower-bending stiffness (including any scaling or tuning factors) and the mode shapes. It does not depend on the gravititional destiffening or the platform or rotor-nacelle assembly (RNA) DOFs, so, it really represents the elastic stiffness only of the isolated tower.
*The generalized mass matrix of the tower depends on the specified distributed tower mass (including any scaling factors) and the mode shapes. It does not depend on the mass of the platform or RNA, so, it really represents the mass only of the isolated tower.
*Because the stiffness-proportional constant is calculated only for the isolated tower, the damping of the tower-bending modes when coupled with the platform and RNA may be different than specified (i.e., the damping ratio derived for the tower-bending modes through a FAST linearization analysis of the full wind turbine system may differ from what is specified for the isolated tower in the FAST input file).
As I know,the Rayleigh damping have two proportional factor about the mass and stiffness.As you said, Fdamping_i = K_ijbeta_jqdot_j
I think the mass is neglected.If not,
I am not sure about the question.Hope your reply.
I agree that general Rayleigh damping includes both stiffness- and mass-proportional terms. For a given alpha and beta, constant for all modes, the end result is that the alpha (mass-proportional) term has more effect at low frequencies and the beta (stiffness-proportional) term has more effect at high frequencies.
However, the tower damping in FAST is not identical to Rayleigh damping. The tower damping in FAST is only based on the stiffness-proportional term and is specified independently for each mode.
I have another question about this topic: when I do simulations the damping that I see in the simulation output is about half of the damping that I specify in the FAST input.
This possibly relates to Jason’s comment in his post above:
To minimize the influence of the other modes I disabled all DOF’s except the tower FA mode. Surely the output damping in that case must correspond to the input damping? Well, I still had the mass of nacelle and rotor not set to zero. Is that fact alone responsible for this factor 2 difference between input and output?
The way I determined the damping in the output was: Turbine running in vacuum (CompAero=false), all DOFs turned off except the first tower mode FA, turbine is parked (so no dynamic damping), initial tower displacement 1 m at the top, then releasing it and inspecting how the amplitude is decreasing.
I did 5 simulations like this, each with a different input damping ratio zeta. I determined the damping from the output by calculating the damping decrement of the decaying tower oscillation.
The simulation results are in the table below (Sorry for the unclear format: it is a table with 1 row header column, 5 simulation result columns and 1 comment column. I could not figure out how to present it more neatly, any spaces and tabs I put disappear).
Simulation 1 Simulation 2 Simulation 3 Simulation 4 Simulation 5 comment
logd 0.01 0.02 0.03 0.04 0.05 Suppose we want these logd’s
zeta 0.0016 0.0032 0.0048 0.0064 0.0080 =logd/(2*pi)
TwrFADmp1 0.159 0.318 0.477 0.637 0.796 =zeta*100 (FAST input value)
x3 9.89E-01 9.79E-01 9.69E-01 9.59E-01 9.49E-01 3rd peak in graph below
x12 9.29E-01 8.64E-01 8.03E-01 7.46E-01 6.94E-01 15th peak in graph below
logd 0.0053 0.0105 0.0156 0.0209 0.0261 =1/12*ln(x3/x12)
zeta 0.0008 0.0017 0.0025 0.0033 0.0041 =logd/(2*pi)
Note the bold numbers, the first bold row is the input logd (which I convert to zeta and % before putting into FAST), the last bold row is the damping determined from the decaying oscillation. There is a factor 2 difference.
Yes, it is the mass and inertia of the RNA that is resulting in a different level of damping in the response than what you input as a damping ratio. The tower damping ratios specified in FAST apply only to the isolated tower, in the absence of the platform or RNA. Effectively, the RNA changes the generalized mass of the tower-bending mode, dropping the natural frequency and requiring a higher level of damping to achieve an equivalent damping ratio when compared to an isolated tower without the RNA. The RNA also impacts the gravitational destiffening of the tower; this term tends to be small, but has more importance the higher the mass of the RNA.
In your case it sounds like doubling the damping ratio for the isolated tower will give the damping ratio you expect for the combined tower + RNA.