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Hydrodynamic response of a semi-submersible floating offshore wind turbine: Numerical modelling and validation Shining Zhang , Takeshi Ishihara The University of Tokyo 2016/11/01
1
/14
• Report in Ministry of Environment (2011)
• Japan: 1600GW for offshore.
• But 80% are in deep water (>50m)
Potential WE in Japan and Challenges
2
0
100
200
300
400
500
0-10km 10-20km 20-30km
0-20m20-50m50-200m
Win
d e
nerg
y po
ten
tial (
GW
)
Distance from coastline
Water depth
2MW (2013) 5MW (2016) 7MW (2015)
• Wave-induced motion • Coupling system
1. In deep water, the best choice is floating type of platform 2. In safe and cost effective design, accurate prediction of dynamic
response of FOWT is necessary
/14 3
Overview of numerical modelling
&a dC C
Force
Motion
Accuracy of predicted dynamic response depends on the accuracy of hydrodynamic coefficients, hydrodynamic models and mooring models
u,u, p
• Morison’s Equation
• Airy wave • Irregular
wave
• Data base • Exp.
Hydrodynamic coefficients
Hydrodynamic models
Wave models
Mooring models
Motion
• Quasi-static model • Dynamic model
/14 4
Hydrodynamic coefficients
• Database (Sachs, 2013; Robertson et.al, 2014, Brennen,C.E.,1982; Haslum,1999 )
– Steady flow
– Interaction is not considered
Hydrodynamic coefficients obtained from the data base needs to be corrected.
Jonkman(2007)
2
4a
aM K b
38
3aM a
/14 5
Hydrodynamic models
• Morison’s equation – Fixed structures (monopile, jacket, etc.)
– Floating structures (Phuc and Ishihara (2007); Marit I. Kvittem et al.(2012); L. Sethuraman and V.
Venugopal (2013); Ishihara et al.(2013))
Conventional Morison’s equation needs to be improved.
0
0.5
1
1.5
2
1 1.5 2 2.5 3
Exp.Cal-Morison
RA
Oheave (
m/m
)
Wave period (s)7.1 10.6 14.2 17.7 21.2
Full scale
Kagaya & Ishihara (2012) Kago & Ishihara (2013)
10-5
10-4
10-3
10-2
10-1
100
101
0 0.2 0.4 0.6 0.8 1 1.2 1.4
Exp.Cal.-Morison
Sz* (
m2/m
2/H
z)
Frequency (Hz)0 0.028 0.085 0.141 0.200
Full scale
F n u u x u x x xt 2 2 2 t t t t t t t t t t t t t t
H b b b t t a a w d d w a a w r0.25π D p -0.25π(D -D )p r C ρ ∀ +0.5r C ρ A( - ) - - r C ρ ∀ -C
/14 6
Mooring models
• Full coupling analysis of Mooring system – Quasi-static model
• Computational efficiency. (FAST ver.8 ,2015; GH Bladed ver.4.6,2015)
• Conservative approach for prediction of motion. (Hall M et.al,2007);
• But, deficiency in tension prediction. (Hall M et.al,2015; Viselli, A.M. et.al,2016)
– Dynamic model (FEM) (Waris and Ishihara ,2012;D. Matha et.al,2011; B.S. Kallesoe et al,2011; Hall M et.al,2011,2015)
• Accuracy has not yet been fully validated by water tank test.
Accuracy of tension prediction should be investigated.
/14 7
1. Propose correction factors to modify the hydrodynamic coefficients obtained from database.
2. Investigate and improve Morison’s equation to predict dynamic response of FOWT with a favorable accuracy.
3. Clarify effects of dynamic behavior of mooring system on tension prediction.
Objectives
/14 8
• Hydrodynamic coefficients from data base
• Forced oscillation test. (Horizontal and vertical)
0.54
0.72
0.75
0.64
0.95
Sachs, P. (2013); Shimada, K and Ishihara T. (2002)
0
0.5
1
1.5
2
1.2 1.6 1.8 2.4 3 4
Ca
Cd
Hydro
dyna
mic
co
eff
icie
nts
To(s)
Hydrodynamic coefficients obtained from data base needs to be corrected according to forced oscillation test
0
0.2
0.4
0.6
0.8
1
1.2
Data base Towing Forced Oscillation
Data base Towing
Water tank test- Cd and Ca
0
0.2
0.4
0.6
0.8
1
1.2
Data base Towing Forced Oscillation
Data base Towing Forced Oscillation
/14 9
• Correction factor for Cd
• Correction factor for Ca
Correction factors- Cd and Ca
Horizontal direction:
Heave plate:
dn
d
i
n 3
i id
Ar =
A sin (θC )
C
n nn n
d d
3
d i d i j d j jt
d t
k d k
C A - C A - C A sin (θ )r =
C A
r r
1.42 ; 0.87n t
d dr = r =
an
a
i
n 2
i ia
∀r =
∀ sin (θC )
C
n nn n
a a
2
a i a i j a j jt
a t
k a k
C ∀ - C ∀ - C ∀ sin (θ )r =
C ∀
r r
Horizontal direction:
Heave plate:
0.85 ; 2.46n t
a ar = r =
-30
-20
-10
0
10
20
30
10 10.5 11 11.5 12 12.5 13 13.5 14
Exp.Morison's equation
CF
x
t*
-30
-20
-10
0
10
20
30
10 10.5 11 11.5 12 12.5 13 13.5 14
Exp.Morison's equation
CF
z
t*
F u u u x u x x C xn nn n n n n n n
a d a
n n n n n n n
H w a w d w a w r=ρ ∀ + C ρ ∀ +0.5 C ρ A( - ) - - ∀ -r C ρr rMorison’s equation:
Correction factors are obtained according to forced oscillation tests and are introduced into conventional Morison’s equation
/14 10
• Free decay test
Effect of unsteady characteristics of Cd and Ca
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0 5 10 15 20 25 30 35 40
Exp.Cal.(W/O Correction)
Dis
pla
cem
en
t-S
wa
y(m
)
Time (s)
0
2
4
6
8
10
12
14
16
Exp.Cal.(Dynamic model)
Natu
ral p
eriod
T(s
)
Surge HeaveSway Roll Pitch Yaw
1. Predicted amplitude and natural period are improved with corrected hydrodynamic coefficients.
2. Predicted natural period in 6 DOFs show a good agreement with that obtained from Exp.
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0 5 10 15 20 25 30 35 40
Exp.Cal.(W/O Correction)Cal.(With Correction)
Dis
pla
cem
ent-
Sw
ay(
m)
Time (s)
/14 11
Regular wave Irregular wave
-5.5%
10-5
10-4
10-3
10-2
10-1
100
101
0 0.2 0.4 0.6 0.8 1 1.2 1.4
Exp.Cal.(W/O F-K)Cal.(With F-K)
Sy*
(ra
d2/m
2/H
z)
Frequency (Hz)0 0.028 0.085 0.141 0.200
Full scale
Pitch
The improved Morison’s equation has been validated by the water tank test
32.5%
zheave
ARAO =
H 2
0
0.5
1
1.5
2
1 1.5 2 2.5 3
Exp.Cal.(W/O F-K)
RA
Oheave
(m
/m)
Wave period (s)7.1 10.6 14.2 17.7 21.2
Full scale
0
0.5
1
1.5
2
1 1.5 2 2.5 3
Exp.Cal.(W/O F-K)Cal.(With F-K)
RA
Oheave
(m
/m)
Wave period (s)7.1 10.6 14.2 17.7 21.2
Full scale
0
0.5
1
1.5
2
1 1.5 2 2.5 3
Exp.Cal.(W/O F-K)
RA
Opitc
h (
rad/m
)
Wave period (s)
7.1 10.6 14.2 17.7 21.2Full scale
0
0.5
1
1.5
2
1 1.5 2 2.5 3
Exp.Cal.(W/O F-K)Cal.(With F-K)
RA
Opitc
h (
rad/m
)
Wave period (s)
7.1 10.6 14.2 17.7 21.2Full scale
10-5
10-4
10-3
10-2
10-1
100
101
0 0.2 0.4 0.6 0.8 1 1.2 1.4
Exp.Cal.(W/O F-K)Cal.(With F-K)
Sz*
(m
2/m
2/H
z)
Frequency (Hz)0 0.028 0.085 0.141 0.200
Full scale
Heave
Pitch
Heave
F n u
u x u x x x
t 2 2 2 t t t
H b b b t t a a w
t t t t t t t t t t t
d d w a a w r
0.25π D p -0.25π(D -D )p r C ρ ∀
+0.5r C ρ A( - ) - - r C ρ ∀ -C
Heave plate:
F nb
t 2 2 2
H b t tb0.25π D -0.25 )pπ(D -Dp
Slender members:
Effect of axial Froude-krylov force
/14 12
Effect of dynamic behavior of mooring system
Quasi-static model
Dynamic model ML1
0
2
4
6
8
10
12
14
16
1 1.5 2 2.5 3
Exp.Cal.(Quasi-static model)Cal.(Dynamic model)
RA
OT
1 (N
/m)
Wave Period (sec.)
Full scale7.1 10.6 14.2 17.7 21.2
Tension prediction by dynamic model is validated by water tank test
-20
-15
-10
-5
0
5
10
15
20
14 14.5 15 15.5 16
Exp.Cal.(Quasi-static model)
t*
T1*
-20
-15
-10
-5
0
5
10
15
20
14 14.5 15 15.5 16
Exp.Cal.(Quasi-static model)Cal.(dynamic model)
t*
T1*
10-3
10-2
10-1
100
101
102
103
0 0.2 0.4 0.6 0.8 1 1.2 1.4
Exp.Cal.(Quasi-static model)
Frequency (Hz)
ST
1* (N
2/m
2/H
z)
1F
2F
3FSurge
Full scale0 0.028 0.141 0.2000.085
10-3
10-2
10-1
100
101
102
103
0 0.2 0.4 0.6 0.8 1 1.2 1.4
Exp.Cal.(Quasi-static model)Cal.(dynamic model)
Frequency (Hz)
ST
1* (N
2/m
2/H
z)
1F
2F
3FSurge
Full scale0 0.028 0.141 0.2000.085
0
2
4
6
8
10
12
14
16
1 1.5 2 2.5 3
Exp.Cal.(Quasi-static model)Cal.(Dynamic model)
RA
OT
2 (N
/m)
Wave Period (sec.)
Full scale7.1 10.6 14.2 17.7 21.2
n n n n n n n n n n n
H w a a w d d w
n n n n n
a a w r
=ρ ∀ +r C ρ ∀ +0.5r C ρ A( - ) -
- r C ρ ∀ -
F u u u x u x
x C x
/14
A fully coupled nonlinear simulation tool, CAsT, is developed with improved Morison’s
equation, and the predicted dynamic responses of FOWT are validated by a water tank test.
The conclusions obtained are as follows:
• Correction factors for added mass and drag coefficient are proposed and used in the
improved Morison’s equation to account for the unsteady characteristics of
hydrodynamic coefficients.
• Axial Froude-Krylov loads on slender members are crucial in prediction of dynamic
response of FOWT. The conventional Morison’s equation is modified to take this force
into consideration. As a result, wave-induced response in waves are improved.
• The dynamic model successfully reproduced all the harmonic components of fairlead
tension measured by the water tank test, but the quasi-static model only reproduced
the first three peaks. This indicates that inertia and nonlinear drag force on the mooring
system have to be considered when evaluating the fairlead tension in mooring lines.
13
Conclusions