Doift UniversilY of TechnOoy
Ship Hydromechanics
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ØTDRODTIAMIC )CDß AID
mELI
UYLUU
01 ADV RESiSTANCE PRKDICTICMSGrant E. Beam, HydrocèchafliCa Beseareb Group,
Koon Chung Tong Department of Naval Architecture and Shipbuilding,
Slew Mtng Lau Univéraity. of ewcastle upon Tyne. UK
£BSTEACT
This paper is principally concerned with the application of alternative
hydrodyTlaatc modela to determine the first and second order wave induced fluid
loadings on advancing oscillating structures. Both near field and far field
added resistance calculation procedures ame presented. For the first tine
full 3D hydrodynsaio interaction analysis are used in otudying the added
resistance of ship forms. Predictions of the bydrodynaniC coefficients, the
motion responses and the added resistance are coepared with experiment.al
easureflt5 and strip theory predictions. The limitations of the different
applied procedures is discussed.
ImoocTI01
A vessel advancing in waves experienCes a resistive force additional, to
that due to its advance in 5tiIl water. This additional force, termed the
added resistance in waves, can also be viewed as the steady second order
longitudinal force induced by the incident waves and the resulting motions of
an advancing vessèì.
The theoretical calculation of the added resistance of a vessel in regular
waves generally falls into two categories. In the near field approach the
8dded resistance is evaluated by direct integration of the dynamic pressure
acting oc the vessel's wetted surface. In the tar field approach the added
resistance is derived froc conservation of the total energy or the total
mocentum of the fluid.
Bere we. consider the influence of a generalised 2D and two 3D fluid
structure interaction analyses on the predictions of added resistance. The
generaliséd 2D based method is cccbined with the near field prediction
t.chfliqUC.
In the first 3D methOd (methodi) the near field approach icombined with a low forward speed 3D hydrodynasic aingularity analy3is. In
the alternative 3D method (method2) the far field approach is ccmibined with a
3D bydrodynamic translating pulsating singularity distribution model. In
etbod 2 pitch fluid damping predictions are very important to the prediction
of added resistance. Therefore the added resistance predictions are repeated
jth 3ust the theoretical pitch fluid damping replaced by its experimentally
.ea3ured value. These calculations arè designated method
2E. The 3D
enhancements developed by the author3 thus permit, for the first tine,
comparIson of experimental measurement3 with 2D near field, 3D near field
arid 3D tar field predictions of added resistance.
2. PASIC FLUID
MDDIS.
To make the near field and far field exact theories applicable certain
choices regarding the exact manner of undertaking the solution of the forward
speed ship motion problem must be made. The full 3D interaction analySis can
be formulated as a perturbation of the steady advancing or wave caking
resistance problem'. However unlesS simplifications are introduced both the
rigid body motion and the fluid structure interactiOn problems would have to
be solved simultanèously in the time domain. The introduction of perturbation
expansions and consideration of fluid behaviour on the instantaneous free arid
wetted surfaces in terms of fluid behaviour on the surfaces associated with
the steady fOrward advancing problem leads to a first order perturbation
formulatIon of the unsteady potential. However the steady and unsteady
potentials also interact in this model through complex inhonogeneous boundary
conditions which häve to be satisfied on the moving surtaces(1). Further
simplifications are required to make the problem formulation tractable. The
fluid structure interaction model to be used thus requires neglecting the
interaction of the steady and unsteady potentials.
Bere ve proceed directly to the statement of two alternative simplified
linearised 3D formulations for an advancing vessel in waves. That
is, denoting
the time independent incident, diffracted and radiation potentials by $, D
and ,k we are required to satisfy:
V2($D,
k)
= O everywhere in the fluid,
32 k
[ g . U2 +
2 iw U w2 J ( ) = O on z = O, e e. D 3x ax on S,, where mk = O k = 1,2,3,, n = n3, and n = on SW. (A) 303It is aleo necessary that
and k 0 as z
- and satisfy an appropriateradiation condition at large distances fron the vssel.
Within the literature Fosulation (A) is usually sisplified using
slenderness assumptions to reduce the 3D interaction analyses for O to a
equivalent set of 2D roraulations. Here we solve the equations as stated and
also provide a second. 3D alternative analysis by assuming that the forward
speed is auch that
u
L
«
ax
Consequently defining the set of potentials as satisfying the wetted
surface condition
= : k=1,2,..., 6
it
follows
thatk:1,2,3,11, With $ = a and = y5
The alternative sinplified 3D analysis thus corresponds to satisfying
=
2 8
-
W 1O everywhere in the flüid,
) O On z = O,
asD
a1
-.!iwn.
ex
and
-an an
Also and O as z + - and the potentials satisfy the Somerfeld
radiation condition.
For the head sea condition a special diffraction analysis
ut be
developed for the equivalent strip theory approach based on the assumptions
of formulatiofl (B). This is not repeated here since it has already been
published
insôe detail(2)
Fr here on there is no need to differentiate between the velocit.y
potential predictions based on the foraulations (A) & (B).
FLUTh STRUCTURE iaiuWTION JMALYSIS
One partcular approach to solving the 3D interaction problems posed is
the source distrlbütion technique based on the identity
= f
O(
G(x;) d$()
+I
0k)c(x;
ndy,
S I
for Formulation (A). For Formulation (B) the second term, representing the
waterline integral, is inappropriate and unneccssary. The coaplexity of the
on the mean wetted surface.
Oreen function G selected
in each case will autocaticillY
echo the
r.quireeants of the aelected formulation.
Thus in Formulatlofl (A) the source
strengths, , relate to translatifl
pulsating sources distrIbuted over the
wetted surface f the vessel.
Whereas in the sinpier Formulation (B) the
source strengths, 0k' relate to
aource3 pulsating at the wave encounter
frequencY. We assune tram this point onwards
that the indicated radiation and
diffraction potentialS are
available, together with the means of processing
th to provide hydrodYflamiC
reactiVe and active coefficients and the motion
nalySi5
of the vessel. With the potentialsand motion responses known the
¡econd order mean forces can be evaluated.
FI..D gLu1T1ON
OF SEcOND ORDER MEAN FORCES..Faltinsen et.ai have derived an added resistance
formula applicable to
any wave direction based on
integration of the near field pressure using strip
theory. The analysis is
identical, except for the forward speed correction,
to second order drift force calculations
on stationarY vessel. Beam and
Tong2
bave generalized the near field5econd order force expressions and
shown that the added resistaflóe can be expressed as
2 P 1
Ira
g dl -p f
I V41$ Ti dS Bet81F'
) L SW-
f
Imt Vs1] FL dS - p U J Retß Vç ) Ti dS la la lx S pg AWXcf Ret1, 6) 1c ... (i)where the first order force term is given by
-
p5 (
-
dS Pg(0,o,n3Aw-fl5Axr) ... (2)
and we bave introduced thé term
2 2 1/2
N =
(i1
n2, n3) / (n1n)
...
()
to account for the slope of the wetted
surface at the free surtace2).
Evaluation of Equation (1) is critCallY dependent upon the
solution of
the first order velocity potentials and the notion responses.
5.
Tar
Field EvaluatiOn of Second Order Mean Force.Mruo'
derived a theoretical formula for the added resistance based Oflthe far field approach. The formula is valid for any wave
length and head
but i difficult to apply directly.
However, by introducing slenderness
8sSuSPtiOflS, the formula can be reduced
to an integral involving the so called
Using the conServation of mcentum approach, some involved integral
transforms and other manipu1ations5, and Nèwn'a6 áymptotic limits tor
the potentials
and D lt
can be shown that the added resistance isexpressible in the. form1
cl
with. =
- K2
source st.rength distributions
boundary value problems(1,2). the fluid flow and associated
can be evaluated. From the
coefficientS and First order
,a) =
°k exp(c) exp[-ic (
SW
I - 2i COSQ ±
I
i - III
cos.32 eos2 a
hence the mot-ion Iesponses predicted.
Since no assumption has been made regarding the dimensionality of the
solution domain in which °k or are to be determined we may now use, in
principal, either of the added resistance prediction techniques. Here the
possible combination of hydrodynamic model and second order force predict-ion
technique is confined to the three approaches defined in the introduction 306
cosa + r ama)) dZ
o
-For convenience 07 is used to denote the source strength associated with the
diffraction potential.
The term can be identified as. the contribution from the interactions
of the incident wave potential and the body potential, whereas the term RBB is
due to the interâction of the body potential with itself. By body potential
we mean the sum of the radiatioñ änd diffraction potentials.
6.
oRcÀrrshTIc4
OF CILCUUTIO«SFor each identified fluid structure interaction mode]. the first order
can be determined by solving the appropriate
Subsequently thé velocity potential arid hence
longitudinal
rates of change of fluid velocity velocity potentials the hydrodynamic reactive wave excitation forces. can be determined andR ; RIB RBB
- pw
where RIB
st cw
Re (H(k,ß)) cosS1/2
31/2 cosa ... (14) ... (5) RBBL {[
J 8! -1/2 +f
+J
)IH(m,a)l .-. a0 1/2/1
-¡It COS
,
:1_cL0 H(IC2,)I2 d } . - ...(6)
v/i -
4t cosawhere = Uwe / g, k = w2 / g and a0 is vero for ( 1/14 and eqûals
arc cos(0.25/r) for i > 1/14. Here the generalised Kochin function B is. given
by
b nkHk
H,
... (7)- i
omputeP based analysis techniques can be used
to provide two quite
diltiflOt sets of calculations.
The first set may consist of those results
jcb ca1 be directlY compared
with measurable physical quantities. Thus
(itbin imposed space iimitation5) ve can
compare the predicted hydrodynamic
r.actt coefficients,
the motion responses and the added resistance with
experimental measureeflt5.
The second set of calculations may be considered as those
intermediate
result5 or copofleflt5 of B measurable quantity
which may not itself be
directlY or indirectly measurable.
The expressions for the second order
forces can be split into a number of identifiable
components. Thus in the near
field formulation, Equation (1), six
components can be readily identified. It
would be very difficult to separate out
these components in an experimental
programme. the other hand within
theoretical predictions it is possible to
provide measures of each component whilst producing the required
total added
resistance. For example the relative contribution of these components for the
Viober's tanker model of CB = 0.85, has been previously
published(1), and it
is known that the first term, representing the contribution
of the changing
vetted aurface area due to the
relative free surface elevation, is the
dominating contribution. In the case of method
2, EquatiOn (il), we consider
the partitioning of the added resistance into (a) RIB and RBB
components and
(b) the subdivision of RIB into heave,
pitch and wave diffraction components.
It is often this second group of calculations
which provide insight regarding
inequalities observed when comparing predicted and experimentally
measured
values.
The particular applications considered in this paper are
limited to the
Series 60 parent form for block coefficient, %,
values of 0.6, 0.7 and 0.8
and a finer form container ship. For each increasing
CB value, for the
Series 60 forms, the Froude number (FN) in each analysis is
decreased from
0.266 to 0.2 to 0.165. For the finer container ship model SR-lOS with
CB = 0.559 the Froude number is 0.2.
8. D1SJSSIOI OF RJLTS.
The added resistance predictions for the 3
Series 60 forms and the SR 108
model are presented in Fijures 1- respectivelY.
In Figure 1, corresponding
to a C8 0.60, two setS of experimental results taken
from Strom_TeJSefl(6)
and SibUl(8) are coopared with the two 3D
interaction analyses of Newcastle
and th 2D predictions of Gerritsma(1) and Salvesen(h1).
In this particular
caSe the heuristic approach of GerritSma(1)
provides a significantly larger
peak added resistance prediction. In fact all
resistance values exceed thé experimentally measured peEk values used. The
lowest theoretical peak value of added resistance is predicted using method 1.
ID
Figur. 2, corresponding to a CB
0.70, we again use the experimental
aeasurenta of StromTejaen
anderritsma0)
but now present the enhanced
2D method
pr.dictions(2),
the 3D method
i
predictions together with three
sets of predictions based on method 2.
This last group of predictions uses
two distinct discretisations and
for the more refined discretisations the
added resistance predictions have been repeated with the theoretical value of
pitch fluid damping replaced by the experimental value of Gerritana(10).. We
now note that the so called method i
and method 2 based on experimental pitch
damping provide, the lowest peak added resistance values. These two sets of
results also
agree quite
closely until
considering
the
higher encounter
frequency regime.
In this figure we note that the 3D rnethod
i compared with
the 2D implent.ation leads to a more significant improvement in the added
resistance predictions than the doubling (almost) of the number of facets in
method 2.Algo,
replacement
of
the
theoretical
fluid
damping bythe
experimentally measured values has more influence on
method 2 than increasing
the
levêl
of
discretisation
in
the
numerical
model.
In
Figure
3,
corresponding to a CB = 0.80, we again compare
StrÖmTejsen(B) experimental
measurements with the prediction of Gerritsma(10) and the two 3D procedures
using oomparable levels of discretisation.
Again,
there is a significant
difference between the 2D and 3D predictions although the difference between
the
two 3D method
is
almost negligble over most of
the. frequency range
investigated.
In
Figure
, we comparethe
experimental measurement of
Fu3ii12
and Nakamura(13)together with the 2D
theoretical predictions
of
Takagi(1)
andGerritsma(1) with the two 3D based
methods.In this case
method 2 predicts
a peak value
twice
the
size
of the other theoretical
predictions and experimental measured values of added resistance. Thus froc
Figures
1to 3 we might have been lead to consider that rnethod 2 became more
unsuitable s.s
it was applied to vessels of fuller
form. However, this thèsis
is quickly disposed of when considering the highly questionable values for the
fairly fine form of the containership rnodel SR-108 ie. a
C8 value of 0.559..
In an attempt to explain the differences between the predicted values of
addedresistance generated
from
the
two 3D based methods we consider In
Figures 5 &
6 and Figures 7 & 8 respectively the hydrodynamic coefficients
and the motion amplitude predictions for heave and pitch. In each of these
four sets of results we compare the experimental measurements of Gerritsma(10)
with the predictions of the 2D and 3D implemented versions of Formulation (B)
together
with
the
predictions
of
Formulation
(A)
for
twodistinct
discretiSations. From Figures 5
& 6
the greatest differences exist in the
fjnent of the discretisation in Formulation (A) does little to improve the
predictiVe capability. In Figur. 7 the heave amplitude response
is more
,enaitive to the hydrodyflamic analysis used tri the lower frequency regime.
When considering the pitch
motOfl
amplitude in Figure 8 someimprovement in
te
predictions of FormulatiOn (A) are brought about bycombining the finer
discretisattön with the experimental damping values,
although once again the
less sophisticated Formulation (B) provides
predicted values luch closer to
the experimental measurementS.
In Figures 9 & 10 we consider the relative magnitudes of the
two
components of added resistance identified in Equation (a.) together with the
proportional make-up of the RIB components attributed to heave, pitch and
wave diffraction. In Figure 9 the effect of refining
the diacretisatiOfl and
the replacement of the predicted radiation damping by the
experimentally
measured pitch damping upon the two compOnents of added resistance is
clearly
seen.
The effect or experimental pitch damping is relatively more significant on
the RBB than the RIB components of the added resistance. This
is to be
expected since the BB term, Equation (6), i
quadratically dependent upon
the motion response whéreas the RIB term, Equation (5), is linearly dependent.
The dominant feature of the pitch motion contribution to the added resistance
is also evident in Figure 10. At the peak of the Ourve the pitch motion
contribution in the RIB component accounts for about 67$ of the total added
resistance in head waves. In bow oblique waves the pitch motion renains
dominant arid those contributions from the lateral motions (not
illustrated)
are very small.
9.
UaUSI0S .AD flIAL
cOP9TS.
Application of the arid 3D based hydrodyflamiC interaction analyses based
on Formulation
(B) and the 3D based FrmulatiOfl (A) indicate:3D effects are particularly noticeable in the hydrodyflamic pitch
damping arid the heave and pitch otiori predctiOfl5,
use of a more exact mathematiCal fluid structure interaction model
does not necessarily lead to closer agreement between predicted
values arid experimental measurements, and
the influence of the discretiSatOfl levels is more apparent in
Formulation (A) ba5ed predietiöns than in
Formulation (B)
When the two 3D bydrodyflamio modele are
reapeotivelY linked with the near
f ild and far field added resistance formulatiOfla, as per methode
I and 2,
then
(iv) the 3D based near field applicatiODS provide
a significant
improve-ment over' the based predictions, Newcastle and others, and is
much
supörior to
th
3D based far field method implemented,Cv) the need to obtain good pitch damping coefficiente
Is clearly evident
from the edded resistance results based on the use of experimentally
measured dampiflg,
(vi) the pitch cponent of the R
term je dominant, and
(vii) the assumption made in other
body-body interaction component
wave-body interactiOfl component
the ship forms examined.
analyses e.g. saivesen(11), that the
is lese significant than the incident
has been demonstrated to be true for
In view of the fact that the amplitudes of the added resistance
determined
from method I and 2 are not always compatible it would be
useftIl to partition
the added resistance determined by' thod i into
the same components
considered in method 2. This would not be the normal partitioning of
the near
field approach but provided due care was taken then it would be possible to
undertake these calculations by carefully suppressing each motion in
turn
within the added resistance post_processing program
and then deducing the R
and terms through a judicious application of
algebra.
lo. acx0LÉD?TS.
The authors wish to acIaowledge the Science and
Engineering Reseàrch
Council
fOr the financial support received to undertake part of'the work
reported in this paper. Part of the support comes
through the SERC Marine
TechDolOgy Directorate industrially sponsored
"Compliant Systems" Cohesive
PÉ'ogramme which made development of' the near field analysis possible
and part
through an SERC Studentship awarded to the third author.
Finally, Kay Thomas
in
thaDked for her patient typing and editing of this paper.1. Searri, G.E., Tong, K.C., and Lau, S.L
'Sensitivity of Wave Drift ramping
Coefficients to the Hydrodyflámic Modela Used
in the Added Resistance
Gradient Method". proceedings of the Offshote
Mechanics and Arctic
Engineering Conference. Houston, March 1987.
2. HearD, G.E. and Tong, K.C.
'EvaluatiOn
of Low
FrequencY Daaping',proceedin&3 of the Offhore Technology Conference. Paper
5176,
Houston, May1986.
. $arUO, L 'The Excess ResiStance
Dt
a Ship in Rough Seas'.International
pujldinA Progre!!., Vol. No.
35, July 1957..
NarUo. L Resistaflce in Waves'. Japan Society of Naval Architects,,
60th AnniverBary Serica, Vol.
8, 1963,
Chapt. 5)iecan, J.N. 'The Damping and Wave ResiStance of a Pitching
and Heaving
Ship'. Journal of Ship Research, June
1959.
Faltinsen, O.M., )4insaSS, g., Liapis, N. and Skjôrdal, S.0.
'Prediction of
Resistance and Propulsion of a Ship in a Seaway"..
!toCeedi50! the 13th
Symposium Naval Hydrodynamics, Tokyo,
1980.
e.
Str-Tejsefl, J., Teh, N.J. and Moran, D.D. "Added Resistance in Waves'Transactions of the SocietY of Naval ArchiteCt5 and Marine Engineers.',
Vol.81,
pp109-lO, 1973.
SIbul, O.J., 'Measuraments and CalCUlatiOñ of Ship Resistance
in Waves',
College ot gjfleering.Ufl1Ver5itY of California. Berkeley..
Report No. Na-71-2,
1971.
Grritsma, J. and Beulcelman, W. 'AnálysiS of the Resistance Increase in
Waves of a Fast Cargo Ship', International $hjpbuildiflg Progress
Vol.19,
pp2B5-283, 1972.
Salvesen, N. 'Added Resistance of Ships in Waves', Journal of HydronautiCs
Vol.12, No.1, pp24-3,
1978.
FujIl,
H. and Takahashi, T. "Exporinental Study on the Resistance IncreaSeof a Ship in Regular Oblique Waves', Proceedings of the 1th International
TOwing Tank Conference. (ITTC),
pp351-3&O,
Ottowa,1975.
Nakaura, S. "Added Resistance and Propulsion Performance of Ship in Waves",
The InteÌnationai Séinár on Wave ResistanCe,
pp199-216,
Japan,
1976.
lE Talcagi, M, Hosoda, R. arid Shimasaki, H. 'An Improvement for the Calculation
of Added Resistance in Waves', Journal of Kansai Society of Naval Architects.
of Japan, No.11,
pp33, 1971.
,
I.
o Il. oii
T W Dt)
z 123
Q IL h % IL. .00
Figures 1 & 2 Comparison of Predicted and Measured Added Resistance.
25 _o ÀOOEO .PSLSTANCE 3EPIS 60 I&1 OP C 0.60 vAv ,*AOIIc. PN 0.266 (XPT. ISIJIjLI 20.0 0 -AODEo PESISTANCE
.3PIS60JI.LL
C. 0.?
NAY! IA0II 1W FN - 0.2 tXPt (PI MRPIV9IA) 70 TPV vCAST.-20 tOQ GEQIT9l* 20 ?f(T, 5ALVESN 266 F*ÇT_ I 06 FACE?- 'DCO 2
I
I'
:(.26 FACt? - &26 FAUT - ITPO E
-o, -(I 20a ISjO
I % I iz
w LI Lt w (J u) (Jz t-
u-I Lfl Ui: Cr D W LI O 6 ADDED RESISTANCE 2 o I, (T '5._0 12.5 o 10.0 p.-z
Ui LI u- D L) _uJ LIz
I 5.0
u, W D W Q (3 AODEO RESISTANCE 5P-108 crIPSHIP V*vt tA0IN& 160 FN. 0.20 o EAPT (NAXA*6) XPt IFUJIII
- - 20 ll*l'
,*XAca - - 20 DXÓPY GPQLTSNA- 30e. FACET - ItT II I
Ó.FACFV - I1 ''2 0.0 3 S 6 0 I 2 3
og
0g
P-'Figures 3 & 4 Comparison
of Predicted and
Measured Added Resistance.
S(PIES 60 UJL 0F C 0.60 VAVt PÇAOING FN 0.165 12 U EXPl t3tP0PI..YEJ,WI -20 TIÇT, &QQITSMA 296 tACET -T
''
I p. ai I0'I
-I a) p.p., aiI
-
_..SIF*CET -J :1 I Cr CrIi
I II.4, o 'O :HYDROOYNAM ÍC COEFFIC.! ENTS 5&QIES 60 I.LL flf! c 0.:?0 EAV COEFcICIEJS FN.0.2 .1 2 wJL3/q 3, p S ií
r.
-2 3 4wJL /g.
o EEPT -- -- .--.O AVCASIL( ._..-.126' FACET' - PTID i 216 FAUT -THQQ 7 e.76 FACET -TPjO 2 5 50H o PÓbYNAMIC COEFF IC lENTS
3PIS 60 IU..1
.0 '0.70
PlTOq C009CIEIII
FN
0.2
Figures 5 & 6 Comparison of Predicted, and
Measured Hydrodynamic Coefficient..
s 0.10,. o. 00 '0.06 0.04 0.02 0.00 0.20 0.15 0.10 0.05 0.00 '0 o
o 'ta'
-. 2T6 FACET .s A26 FACET s'. s S ss b -I - . .5 1 a a u e/ /
o --.6 -. s505s..q..e
ìss
/
1
/
u.
S'-.'
s.
I 2 .3.
wJt/g
3 7u.
a 2 if s s oMOTION AMPL I lUDE
SERIES 60HUU. OF C 0.70 VAVEHEAOING lO FN - 0.2o
FXPT - GFPRITSMA -NEWCASTLE 226 FACET -METHOD I ----316 FACET - 'METHOD 2, "26 FACET -METHOD 2-/o
-.----'
-4 2 3 45
6wIL/g
MOTION AMPLITUDE
SERIES 60 NUll OF C 0.70 WAVE HEADING ted' FN -0.2Figures 7
R Comparison of Predicted and
tÇeasured Motion Amplitudes.
o E1IPT - 'GERRIT9(A
--21) - HEVCASTLE 226 FACET - HETP0 t 316 FACET -TMOO 7 26 FACET -Z 26
FACET - ItIPW 2E'
2.5 2.0 I.5 p-, / /