8 JAN. 1916
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Ship 192
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September 1975
National
Physical
Laboratory
Ship Division
u e uEXPERIENCE IN COMPUTING WAVE
LOADS ON LARGE BODIES
Reprint of paper presented at the
Seventh Annual Offshore Technology
Conference, Houston, Texas. May 1975
by NG Hogben and RG Standing
SMTR-7523
Extracts from this report may be reproduced
11PL Ship Report
192
September1975
NATIONAL PHYSICAL LABORATORY
PERIENCE IN COMPUTING WAVE LOA])S ON LARGE BODIES
Reprint of paper presented at the Sevénth
iva Offshore Technology Conference, Hpuston, Texas.May
1975.
by
OFFSHORE TECÑNCLGCY CONFERENCE
6200 North Central Expressway
Dallas,.Texas
75206THIS PRESENTATION IS SUBJECT TO CORRECTION
Experience in Computing Wave Loads on Large Bodies
N. Hogben and R. G. Standing, Ship Div., National Physical Laboratory ©Copyright 1975
Offshore Technology Conference on. behalf of the American Institute of Mining, Metallurgical, and
Petroleurr Engineers, Inc
(Society of Mining Engineers, The Metallurgical Society and Societ1 of
Petroleum Engineers), American Association of Petroleuir Geologists, American Institute of
Cheffi-cal Engineers, American Society of Civil Engineers, American Society of MechaniCheffi-cal Engineers,
Institute of Electrical and Electronics Engineers, Marine Technology Society, Society of
Explor-ation Geophysicists, and Society of Naval Architects and Marine Engineers.
This paper was prepared for presentation at the Seventh Annual Offshore Technology
Conference to be held in Houston, Tex
,May 5-8, 1975
Permission to copy is restricted
to an abstract of not nore than 300 words
Illustrations tray not be copied
Such use cf
an abstract should contain conspicuous acknowledonient of where and by
hoir the paper is
presented.
PAPER
NUMBEROTO 2189
ABSTRACT.
Designers of offshore installations for the North Sea and adjacent waters face a number of
exceptional demands specially regarding the extreme and continuing severity of the weather and the large watér depths. In response to this challenge, there has been rapid development of new design concepts and a major trend already well established, is f 9r the emergence of new types of large monolithic structure. These pose many difficult design problems and, in
particu-lar, are. not genér1ly amenable to conventional methods for estimating wave loads. For such
structures, prediction methods based on diffraction theory are needed.
INTRODUCTION
This paper describes eerience in ship
Division. of the National Physical Laboratory in the development, validation and application of a computer program written for this purpose that has been supplied to a number of computer bureaus and to Lioyd Register of Shipping and has been extensively used by.the offshore
industry. This work has been undertaken as part
of a research program approved by the Ship and Marine Technology Requiraments Board. Some
earlier aòcounts have already been published in Ref
5.
1 and 2, the first being mainly concerned References and illustrations at end of paper.with the computer program development and, the second with experimental validation and
preliminary operational experience. The present paper recapitulates the salient results of the
earlier' publications and reports recent progress including some further experimental results, but emphasizing the more .extensive experience since
gained in practical applications of the computer program.
Before discussing this experience in detail it may be helpful to be mo±e specific
about the nature of the structures concerned. The term monolithic used above is intended in this context to refer rather loosely to a. range of structure tpes that are 'very diverse in
configuration. All, however, contain at least one component' which is very much larger in diameter or equivalent section dimension and often quite complex
in
shapè compared with the normal tubular components of a steel jacket, It is because of these features that diffraction theory methods of wave loading analysis are generily needed in fact for reasons that areexplained iii detail
in
Ref. 3 and will bebriefly indicated in a later section of this paper. 'In many cases construction is primarily 'of concrete and diameters of the main components may sometimes range up to 100 or 200 mo
L114 XPERIFNCE IN COMPUTING WAVE LOADS ON LARGE BODIES OTC 21
of structure to which this description applies, and these include gravity platforms, tension leg and tension stay structures and storage
tanks. At the time of writing the program has
mainly been used for gravity platforms for which a substantial number of orders have now been placed. The level of demand may in fact be judged from a recent list of UK North Sea Platform Orders4 showing a count of 11 con-. crete gravity structures in comparison with 13
steel jackets. The definitive feature of these
types of platform is that they rest on the sea bed under their own weight without piling.
They commonly consist of a single massive base on which stand a group of three or four towers carrying the platform clear of the sea surface. There is, however, a diversity of actual
geometry as is well illustrated by
an
inter-esting pictorial review of more than a dozen current designsin
Ref.5.
This includes some hybrids involving combination of jacket-typesteel structures on concrete bases.
The program has also been used for at least one tension stay platform, at least one
storage tank and for studying the forces on one large complex-shaped component of a
semi-submersible. For all these types of structure
there is again great divrsity of design. Tension stay platforms, like tension ones re essentii1y floating structures anëhored to the seabed by cables kept in tension by excess of buoyancy over weight. in this case, however, the cables are spread to restrict lateral motion, whereas those of a tension leg platform are vertical. The review Ref.
5,
mentioned above, includes a picture of a tension stay platform consisting of a very large anchored buoyancy chamber carrying a group of towers on which the platform is mounted. Information about tension leg platforms may be found inRef.
6.
Storage tanks may be independent units such. as the Dubai installations described in Ref. 7, grouped like the Ekofisk tank complex,
or incorporated in the base units of avity
platforms or in single buoy .moorings.
Re-garding semisubmersibles, Paulling'P and Hòoftl'l have successfully estimated wave loads
and motions without using diffraction theory. for a number f conventional designs. Diffrac-tion analysis may be needed in some cases however, especially for designs involving very
large unconentionl ly shaped elements or strong interactions between neighboring components.
Many other applications are possible, but the foregoing account covering different
structure types for which the authors have some computing experience should serve to emphasize the versatility of the program and to assist discusion.of some of the special.problems that have been encountered in practice.
9
INTERPRMATION AND VALIDITY. OF PRO.AN
It is essential for effective application of the program that the physical basis of the calculations and the meaning of the output is clearly understood and that reliability is well established. These questions of interpretation and válidation have been discussed in some detail in the two previous papers, but for completeness will be briefly recapitulated in this section.
Accounts of diffraction theory may be
found in Ref s. 12 through 15. . The NPL
computer program uses method of analysis developed by Hess and .Smith-°' and by Garrison
and Chow, 17 which are applicable
to
fixedbodies or arbitrary shape placed in 'a regular linear wave fIeld. The bodies disturb the wave fiéld and èxperience forces 'that combine conventional added mass änd diffracted wave effects.' The computing proáess involves first replacing the body urfaces by a large number
of mál]. plane facets. Computer storage and
run timè limit the number of facets and,
therefore, the resolution of the structure
sur-face. A fluid source placed at the center of
each facet pulsates with the frequency of the incident wave. The ource strengths are. calcu-lated by matrix inversion technique to make thé'volocity normal
to
the body surface zero at each source point. The oscillatory disturb-ance created by the sources represents the scattered wave, which includes the added mass and is superposed linearly on the incident wave pattern. The resulting pressure 'fiêld isintérated over the body surface to' give .the over-all forcés arid moments.
Physical Inteì'pretatjôn'
The physical interprétation of this pro-cess has been discussed in the previous
papers12 and à fuller' account may be found in Ref. 3. For the present a very brief explana-tion will' be given with emphasis on 'showing how diffraction forces relate to conventional
inertia forces 'as define& by Morison' s
equation.18 ' . .
'It is convenient to regard the pressure distribution on 'the body surface and the resulting forces and moments as being the sum of two componénts. The first is the pressure in the undisturbed incident 'wave th'at inte-grates th the force Fj., generlly Ithown as the Froude Krylov force. By an analogy with the Archimedes principle, this force may' be equated to that which would be eeziéncèd by a fluid replacement of the body volume V. Hence when the body spans a small enough fraction of wave length such that the ambient acceleration U is
aprodmately constant, it foUow that Fk = pVU (where p is the' density of water) and may be. regarded as a dynamic analog of. static
buoyancy.:
The second component may be referred to as the disturbance pressure and integrates to the force Fd, which is that due to the disturb-ance of the ambient pressure in the incident
wave by the presence of the:: body. This
includes the effect both of the local disturb-ance, normally déscribed in terms of an added mass term kpVtJ, that edsts even when there is no free surface,:asw]l as: that of the
scattering or diffraction of the incident wave. In fact, when the body spans a small fraction of wave length (less than a fifth say), the scattering term is negligible so that
F :.:kpVU,
It may. thus be found that a diffraction coefficient Ch defined as
=
: (Fk +
may be used to determine the total force F (neglecting drag) on: a fixed body by the for-mula :
:
F ChFk
and for bodies spanning a small fraçtion of wave length V: : C:
h::. ::
1+k
C m and:: : CpV(J : :-where Cm is the conventional mass coefficient as used in.Morison's equation.
For t:he general case of a boy of mass M, which has itself an acceleration U0 and is sub-. ject to an external force Fe, it may be shown as explained in Ref. 3 t:hat:
F CpV (ir - j) + (M- pV) TI It shoiild be noted that some authors. identify mass coefficient with the added mass factor k defined, above and., if this is: now: denoted by C, the foregoing equation becomes
MtJ-.pV_CpV(U_tJ).
These twò more general forms for the inertia force equation become siificant when analyzing cases such as tension leg and tension stay platforms where there is some dynai.c response of the body to :the action of the wave
forces.
-Validation of the Proam
Ref. 1 describes comparisons with some very preliminary :eg)eriments, and with data
from other published work including theoretical results of MacCarny and Fuchs'4 for a vertical cylinder, Garrison and Chow7 for a floating hemisphere, and Gran19 for a gravity platform base, the last named including some comparisons with the results of model experiments. The
comparisons with published data involving pressure distributions as well as forces and moments established confidence
in
the theoret-ical reliability of the program.: Regarding the author' s own experiments these could only be discussed in a rather preliminary wayin
Ref.: i and a much fuller acöount is given inRef.
2
prefaced by a shor:t review of otherpublished work reporting comparisons between theory and experiment. Even in this later paper, the eerimental results could not be reported in full since the test schedule was not finishéd in time. A more extensive set of results is however now available, and for
completeness the following brief review summa-rizes: the over-all picture including recapitu-lation of salient material from Ref s, 1 and 2.
This may be introduced by again quoting some of the references to other published comparisons of theory and experiment recited in Ref. 2. These broadly indicate remarkably good agreement between theory and the results of model experiments but there is little good data for surface piercing bodies with diameters large in comparison with wave length and the only data from full-scale tésts
in
the diffrac-tion regime biown to the authors is t:hat of Brôgren As :mentioned:in Ref. 2, a comprehensive review of published comparisons with model e,eriments is given byCh1OEabarti.2U This presents results for a wide- range of simple geometric shapes taken from. other references, as indicated by the following list using reference ntimbers appli-cable to the present paper, sown beside each shape: Hemisphere,2- Sphere, Horizontal Half Cylinder, Z3 Horizontal Cylinder,24 Rectangular Block25. and Vertical Cylinder.6
Mention should also be made of a paper by Lebreton énd Cormault2? containing results for truncated vertical cylinders and 'to more recent papers by van Oortmerssen28 and by Boreel29 which contain comparisons including pressure distributions'on a square sectiOn surface piercing column on a pyramidal base.
The authors' experiments invòlved measure-ment: of forces, moments and pressures on the family of four circular and four square-section vertical columns of varying height Shown in Fig. i in water depth d =
2.3
m. They broadly confirm the favoráble comparisons with theory reported by other investigators, but have drawn attentiön to some discrepancies occurring in certain cases.The forces and moments were. measured by mounting the test columns on the five component strain gauge dynaniometer illustrated diagram-matically in Fig. 2, which includes a photo-graph of a test cólumn ready for mounting. The dinaniometer was designed by H. Ritter assisted by R. A. Browne, and consists
essenti-V1y of two vertical conáentric cylinders. The inner one is bolted to the tank bottom and the outer one carrying the test column is connected to the inner by a system of strain gauged flexures. Pressures were measured at points on the cylinder surface using flush diaphragm silicon strain gauge transducers, and one transducer was mounted internally on top of the dynamometer to monitor the pressure inside so that the measurements of vertical force could be adjusted accordingly. Some internal pressure variation resulted from the small gap
around the base needed to allow freedom of deflection for the dynamometer. The datà-handling equipment provided magnetic tape records of all signals for subsequent computer
analysis and pen records for display during the experiments.
Measurementsof forces and moments from tests in regular waves over a range of wave lengths for various wave heights are plotted for all the eight coluims in comparison with
curves derived from the diffraction theory program in Fig. 3.
The measurements of vertical force shown have been corrected to remove the effect of internal pressure variation. The results for the four circular columns have already been published,2 but are recapitulated here for
completeness with the perniission of the Royal Institution of Naval Architects. The results for the square section. columns have not been previously published.
It is, unfortunately, not possible to give hère corresponding details of the comparison of pressure measurements with theory due to the large amount of space that would be needed. It is hoped that in due course a fuJ4er acçount will be published, but meanwhile those inter-ested in comparisons of measured pressure with diffraction theory predictions will find valuable data
in
the paper by Boreeì29 men-tioned above.The main conclusions from the experimental investigations may be summarized as follows:
1. The results broadly confirm the experience of other investigators who have found good agreement between diffraction theory and experiment. They are reassuring to
designers regarding the reliability of the computer program since nearly all the experi-mental values for force and moment lie below
the theoretical lines. No systematiò trend has been identified in the scatter of variation with wave height, and it seemS probable that this is a measure of the degree of eerimental
error.
2, In certain cases it rna be seen that
the experimental results for the vertical forces lie well below the corresponding theo-retical lines. This is believed to be due to wavebreaking on the column top causing some loss ofwave height and, hence, reduction of vertical force. This explanation is consistent with the trend of the results, the defect being greatest for the coluimis that caused the most wavebreaking. As might be expected, the square columns are the most strongly affected, especially for the cases h/d = O. and 0.9 when the coluimi top is nearest to the surface, as may be seen in Figs. 3f and g. Regardin the
circular columns only, the results for h/d = 0.9 are affected and the gap is much smaller as shown in Fig. 3c.
The experimental measurements deviated from linear theory in some other minor respects that did not noticeably affect the over-all forces and momènts. In Ref. i it is noted that in shorter waves the wave profile on the front face of the square section surface piercing column rises to a central crest that is much more sharply peàked than the prediction of linear theory, as demonstrated by a comparison using measurements from a photograph of suòh a
wave. This is a phenomenon to be expected for
steep nonlinear wàves and is a form of "clapotis". It haS subsequently been exten-sively observed and filmed on front and rear faces of both square and circular section columns.
Irregularities noted in pressure records from the preliminary expeï'iménts de-scribed in Ref. i were subsequently found to be due partly to spurious thermal effects on the transducers since corrected and also to genuine
second harmonic components'. These are' a Imown
nonlinear phenomena occurring in steep reflec-ted waves and hàve the special property that they do not decay in the usual way with depth. Detailed accounts of the phenomena may be found in Ref s. 30 through 32 and some comments relating to the present investigation are included in Ref. 2. They do not significantly
affect forces ànd moments, but unless their edstence is recognized, they may wrongly' suggest faulty instrumentation.
in the case of the square columns, large vortices were observed at the corners
as illustrated by photographs in Ref. 1. 0riginJ.1y, as indicated in the reference,' it was thought that these might significantly
afféct the experimental results. Subsequent ECPERIEICE IN COMF(JTING WAVE LOADS ON LARGE BODIES
OTC 2i9
417
investigations, however,
inclding somehighly
simplified theoretical. estimates
ofthe
influ-ence. of the vortices on the pressure
distribu-tion, persuaded the authors that the effects should at leasttheoretic11y be
confined tovery
small regions at the. corners. This viewseems to be con.firmed by the good agreement
betweer theoretical and eerimental pressures
reported
byBoreel, 29 even,
nearthe corners of
a square.sectioned column.
COtJTING
EaIErCEThe NFL wave diffraction. program is
docu-mented more fully in Ref s, 1 2 and
resembles other programs described in Ref s. 17,
28, 33 and
34.
It is currently being operated within NFL, by two computer bureaus and by Uo,ds Register of Shipping. As noted in the introduction, it has been applied mainly to gravity structures including storage tanks and production platforms, but also to tension stay and semisubmersible pontoons. Some of the questions that have arisen are of general interest. The remainder of this paper surnina-rizes the authors' eerience of running theprogram
and answering the questions.Section Shape Study
Comparisons were made
inRef. i of tue
horizontal
force, vertical force
andover-turning moment
onsimple
gravitystructures
resting
onthe sea bed..
These were simple
verticalcolumns of
circular,hexagonal and
square
section. The ratio of column height h
to water depth d. was h/d = 0.3. The section
areas were all equal to ita2, where a/d = 0.3. Section shape had little effect on the vertical
foròe,. The horizontal force and moment on the square column was up to 8 percent 'higher than on the circular, the hexagonal column results
being intermediate.
Parametrisation of Forces on Circular Cälumns
For the reasons discussed in an earlier
section, it
s convenient to regard the wave
force on a body as the product of the
F±'oude-Krylov force on that body and a diffraction
coefficient that
takesaccoimt of added masse
as well as wave scattering. Thisbecomes the
conventional mass coefficient Cm in very long waves. For models synùnetric abOut thetwo
planés x = O and y = 0, threç diffraction
coefficients Ch, C
and Cy are defined as theratios of the mad.rnuin total to ma,thnum
Fronde-Krylov horizontal force, vertical force and
overturning moment, respectively.
Values of
C, C. and C
have been computed for a range of
circular columns, of different aspect 'ratios,
typified by their height-to-diameter ratio
h/2a,
resting on the sea bed. The results,tabulated and shown graphicUy in Ref. 2,
Table 1 and Fig..7, are relatively insensitive
to wave length X and water depth d over a range
of large X/a and d/h values.
These cases
include many of interest tO designers of gravity structures, particularly because
sec-tion shape is also comparatively unimportänt
(see section, Shape Study). The results are
reprinted here in Table 1. The original table
also included a phase añgle associated With each force and moment, but these differed little. from t'he corresponding Froude-Krylov
values.
Over most of the range the
coeffi-cients can be
fitted quite well to the
approd.-mate formulae: Ch 1 0.75(h)1/3
(i -0.3 C 1 + 0.74 k2a2.(--) for 1.48 ka (_!L) V 2a ' 2a 1 + 0.5 ka for 1.48 ka (1;) > 1, C = 1.9 -0.35 ka.The range of vàlidity, by comparison
with
theresults of the full diffraction
analysis, isroughly
h/d <0.6
0.3 < h/2a <:2.3 for
Ch and
0.6 < h/2a c 2.3 for C,,.
Over
these ranges the approd.mate formulas,shown in Table '1, are nearly
lJ. less than. 5percent
in error.Over
most of the range, theerror is only
1 -2 percento
The formulas may
be italid
over a greater range ofh/2a, but.no
tests have been carried out.
When h/2a
islarge, both Ch and C
tend to a constant value
close to that predicted by the theory of
MacC
amy and Fuchs and shown as
in Fig. 2 of
Ref.
35.
It must be emphasized that these results are pplicable only to columns resting on the
sea bed. The horizontal force on a suspended
or buoyant cylinder, such as a tension-stay
platform or spar
buòy, is probably similar, but'the vertical force iS completély different, depending on the vértical pressure gradient in the fluid rathei than on the pressuré itself.
The corresponding C. differ.s accordingly, and
in particular becomés very much greater than i
if
h/2ais small.
The analogy
iswith
athin.
disc moving at right angles to its plane,
entraining a large mass of fluid.
Interaction Effects
The velocity potential at angular position e and distance R from the
añs
of a circularcylinder of radius a
in auniform
unbounded < 1,stream, speed U, is
from6
U (. + a2/R) cose
This means that the disturbance velocity decays with distance as a2/R2 and is small for R greater than two cylinder diameters. If a free
surface is introduced. and th cylinder passes
vertically through it, a similar decay rate is expected both in currents far below the. surface and in waves that are long compared with R and a, and can be treated instantaneously as
steady.
The cylinder scatters shorter waves how-ever, and the disturbance field extends much
further. A diffraction program of the type
described Is useful for studying interactions between two or more members of a structure. Lebreton and Cormault,27 their Fig. 9, using the program described in Ref.
33,
calculated the forces on two vertical piles 5 diametersapart. The inaxintum effect was felt upstream
where waves reflected from the downstream pile face combined with the incident wave to form
partially' standing wave pattern, as
in
Ref.28, Fig. 9. The upstream pile experiençéd a madrnurn increase or decrease of force of about
20 percent near ka = 0.6, depending on its position in the other's standing wave pattern. Smaller effects were noted in both longer and
shorter waves, with for example changes of about 10 percent near ka = 0.4. The down-stream pile was less affected, corresponding changes beingless than 5 percent. Piles arranged parallel to the wave crests affected
each other by only 2 percent.
Ref. 2 confirmed the extent of the up-stream disturbance at ka =
0.5e
The wave elevation, according to MacCainy and 'Fuchs'theory, 14 was stil]. 15 percent of the 'incident
wave at R/a = 10. The conclusion, therefore, is that
in
long waves and deep currents,inter-actions are unimportant at radial distances greater than two colurrni diameters, but there seems to be considerable upstream influence at 5 diameters near ka = 0.5 and shorter wave--lengths.
There may also be interactions between
coluimis placed on top of each other.
Calcu-lations in Ref. L showed less than 10 percent difference between the forces on a complete two-coluzini structure and the sum of foròs on the separate components. But in that case the upper coluxmi diameter O.2d was small enòugh in
comparison with the base diameter 0.6d to leave the'flow around the base substantil1y unaffected. The difference is probably greater
if the coluni diameters are similar or if the superstructure consists, of several towers instead of'one.
The Effect of Diffraction, on Wave Elevation
When a wave travels into shallow water, it steepens and its length decreases. A wave' passing over an obstacle experiences a similar
effect, intensified by focusing of the wave rays as they change direction.i7 This means that the wave elevation over the top of a
submerged structure maybe greater 'than that on either side. Desi'iers should take account of this (i) to ensure that thedéck is high
enough to clear the highest waves expected, (2) when computing wave forces because members near
the surface are immersed more deeply
(3)
in considering impact . loads where the wave steepenenough to break. . '
The NPL program can give designers guid-ance because it can provide optionally the linearized diffracted wavè elevations at any' point. This is done by requesting pressure'
output on the plane z = O. The linearized BernoulJ.i equation. for the subsurface pressure
p is' '
p = p ò/òt,
where '1' is the velocity potential and t is
time. On z = 0, the Bernoulli equation gives
the surface wave elevation instead,
=
1à/òtonzO.
Thus, requesting dimensionless pressure p/pgH on z = o in fact gives the ratio of wave elevation to indident wave amplitude /%H. Fig. 4 shows aprofile 'along the 'centerline
y = O of the 'total wave amplitude over the submerged square-section colunri shown
in
'Fig. 1.Here h/d 0.9 and ka = 1.0. The wave amplitudE oscillates upstream where the reflected and incident waves interfere to form a partially standing wave pattern. It decays gradlly to'
the incident wavé level downstream. Also shown is the actual wave profile at the instant when the total downward force is a mad.mum
(phase= 2.22 rad)., Over the top of the coluim, the wave is both higher and. shorter than 'the incident wave. In practice, quite steep inci-dent waves broke at this point.
The Effect of Óurrents
Currents have three distinct effects. First, by changing the fluid particle velocity they change the fluid drag. Because drag depends on the square 'of the.velocity, and 'the current velocity, decreases slowly with depth, a comparatively small current can increase drag siiificant'ly. Because this paper is concerned mainly 'with inertia-dominated situations, this effect will not be discussed further.
The second effect is that of changing the wave speed, the wave propagating over a moving rather than stationary fluid. This may be
associated with wave steepening.3 This effect is small in a North Sea desi wave situation, where, for example, wave period T = 15s, wave speed x/T = 23 m/s, but the madmum current speed is only 1.5 rn/s.
The third effect of a current
i8
to make the structure itself ge±erate waves. A bodyin
a uniform current causes a stàtionary wave pattern to form on the free surface andexperiences a corresponding net force, which may be regarded as a special type of
diffrac-tion force. It is also directly equivalent to the so-called wave-making resistance
experienced by a ship or other body
in
uniform motion through calm water. This fOrce can becalculated by basici ly the same method as the diffraction analysis used in the edsting program, but with a different form of Greent
function that now describes the potential due to a unit source
in
a tthiform current rather than a pulsating soUrcein
still water. Theauthors have examined the possibility of modifying the computer program so that it can
calculate these uniform current forces but decided against it for reasons that are
dis-cussed in detail in Ref. 39 and can only be briefly summarized here.
Although the revised fOrm of Green' s function is laiown and may be foUnd for example
in
Refs. 15 and 40, it is not simple, and substantial effort would be nèeded to make the necessary programming changes. This effort moreover would not be justified because for practical offshore structuresin
realistic currents conventional drag forces due to flowseparation and wake formation effects are dominant and the diffraction forces are not only negligible in comparison, but also deviate grose]iy from the predictions of potential flow
theory. This point is well substantiated by
comparisons for the case of a surface piercing vertical cylinder, between wave resistances computed from theory of Ref. 41 and experi-mental values derived from measured wäve patterns by the methods of Ref. 42.
Fig. 5 summarizes the results. As dis-cussed in the references, the theory lacks i.iniqueness, but using the favored sOlution for cylinders of elliptical section with = b/a as shown, it was found that the ratio Cw/ 2.4 independent of e. when plotted to a base of Froude number je F = c// , where
Cw = wave rsistance/(pAc2) A = projected frontal area c = current spéed
F =
c/f.
The figure shows experimental results for a circular cylinder, a = 1.0, but to achieve even approdmate correspondence with theory it was necessary to assume, due to flow separation and wake formation, an effectively elliptical section with 6 = 0,2. 1Ìi Ref. 39 the relevance of these results to offshore structures is discussed, and it is shown that even for exception11y strong North Sea currents, Cw is negligible in comparison with Cd.
Nonlinearity of the Waves
The NPL wave-diffraction program uses linear wave theory even under extreme design wave conditions. Designers have expressed con-cern about two nonlinear effects. First, are the differences between linear and higher-order theories significant for a typical structure
in
a typical design wave? Forces F on a con-ventional jacket-type structure are usually predicted using Morison' s formula18F =
CpV(J+CapAUjUI
with velocities U and acceleratiOns U given by higher order StOkes43 or stream function theory.44 Skjelbreia and Hendrickson's.Fig. 343 shows linear and Stokes V velocity profiles differing by 20 percent or more at the free
surface. This would indicate differences in
drag of over 30 percent. Is this an extreme example?
Second, where the structure pierces the surface, is it necessary to integrate the forces up to the actual free surface, rather than to mean water level? Conventional linear theory, in particular the NPL program, computes wave forces over a constant immersed depth, the wave pressure field being continued up to or
cut off at mean water level.
Comparisons were made first between linear and Stokes V43 regülar waves
of
the sarnê height H and period T in the same méan water depth d. Some authors prefer to use still water depth instead, the difference being terms propor-tional to H2 and 4, according to Stokes Vtheory. The ratios chosen H/gT2 = 0.015 and
H/d = 0.2, are typical 6f a northern North Sea design wave situation, where for example d =
150 m H = 30 m T 14 s. Comparisons were also made using a less steep wave H/gT2 = 0.01
àt H/d = 0.2. The conclusions were similar,
but the differences smaller. Dean45 compared various anaJ.ytical theories to find the best fit to the free surface boundary conditions. He recommended Stokes V Or stream function theory forthe cases described here. When H/gT2 = 0.015, the linear and Stokes V wave-lengths X are given by x/gT2 = 0.158 and 0.170, respectively. The difference, of some 7 per-cent might be important for a structure
spanning several wavelengths, though norm1 ly
such short waves would contribute little to
the over-ailforces.
Velocity and acceleration
profiles were also computed.
Fig. 6 shows the
these as dimensionless Morison drag an4 inertia
terms, uIup/-H, wPwl/gh,
/g and */g, where
u and w are the horizontal and vertical
veloc-ity components, and
and * are the
corre-sponding accelerations.
Each profile is shown
at its mañmum in the wave cycle.
The
differ-ences between the linear and Stokes V terms
are roughly 20 percent in wßwj, 9 percent in u
which are in phase with wavé slope, but 13
per-cent in uf uJ, 3 perper-cent
in*, which. are in
phase with wave elevation.
This suggests that
the most important effect of nonlinearity is
to steepen the waves rather than change its
elevation.
The differences decrease with
depth, the theories being identical near z/d =
0.4.
There are qmVI differences of opposite
sign
below this depth.
Fig.
7shows the resulting force and
over-turning moment on a slender vertical column of
radius a extending fróm the sea bed below the
origin of coordinates up through th
free
surface.
The linear and Stokes V inertia
contributions, both integrated up to mean
water level z = 0, differ by less than
7per-
-cent of the madmum; the drag contributions by
less than 13 percent.
The load on a typical
gravity structure in a North Sea design wave is
mainly inertial and most of the structure is
quite deeply submerged.
Linear theory is
therefore quite adequate to describe the
over-all loads.
A higher-order theory may be
needed for loca:I loads on drag-dominated
members such as conductor tubes, particularly
near the free surface.
There the structure pierces the free
surface, the error in using linear rather than
higher-order Stokes theory may be rather less
than the error in regarding the immersed depth
as constant.
Fig.
7compares calculations
of the Stokes V force integrated up to the
actual free surface z =
with the forôe tip to
mean water level z = 0.
A similar calculation
using linear theory showed only small dif f
er-ences from Stokes V theory.
In Fig.
7,
the
inertia force and moment are skewed sideways
so that the madma occt2r closer to the wave
crest, but their magnitudes are only slightly
increased. Thus, the main effect
f the extra
wave immersion on the inertial load is a phase
shift of the mañmum.
If the wave is. distorted
by diffraction, the effect is less predictable.
The wave elevation may be increased as well as
thè phase changed (see Fig. 4
for exaple)o.
If the linear diffracted wave elevation is
required this can be output optionily by the
NPL program as elained in the effect o.f
diffraction on wave elevation.
Tald.ng the actual rather than mean
immersed depth has a dramatic effect on drag.
The madmwn in Fig.
7still occurs at the wave
crest, but its maitude is almost doubled.
This effect is most important, particularly in
respect of local loads where drag-dominated
members pierce the free surface.
Ai-i Approdmate Method for Bodies With Wells
Some recently proposed gravity structures
have featured either a protective wafl around
the base or a vertical well extending part or
all of the way. down to the sea bed.
These
present similar problems to the computer,
inthe first case if the wall is too thin, in
the second if the well is too narrow and
deep.-As noted in Ref s. 16 and 2, a satisfactory
computer model of the inner surface arid lip
may require a large number of facets at a
Icorrespondingly high cost.
An inadequate
deséription results in program failure during
matrix inversion or inaccurate results.
Fortunately, it is often possible to cap the
well, correcting for it later.
Numerical
tests .to find a satisfactory correction
pro-cedure were carried out on a simple circular
base with a vertical central well extending
down to the sea bed.
Two approd.znate
calcu-lations of the forces and moments were
com-pared with results from the actual model
including the-well.
The first approdmation
makes the assumption thàt thè water inside the
well is dead and at a uniform but time-varying
pressure.
This means that the well is
effec-tively cápped and the actual body experiences
the same forces as the capped body less the
vertical forces on the cap itself.
The second
estimate comes from multiplying the forces on
the capped body by the ratio of the displace-
-ment volume of the actual and capped bodieso
This approdmation roughly represents the other
extreme where the external pressure gradient
penetrates right inside the otherwise dead
well.
The analor here is with the buoyancy
force on the body turned on its side
ina.
uniform vertical gravitational pressure
gradient.
It may be expected that the forces
on the actual body should lie somewhere between
the two. approximations.
'Fig.
shows the horizontal and vertical
force and the ovei'turriing moment on typical
gravity bases of height h, radius a, well radius
r in water of depth d. Here the ratios dfa'=
3, h/a
0.
and the two wavelengths chosen àre
ka = 0.5 and 1.0, where k
= 2tJX.
The results
are plotted as functions of r/à, small r/a
representing a narrow deep well that hardly
affects the forces, r/a close to 1 representing
a thin protective wall on its own.
As was
hoped, the forces and moment on the actual model
lie between the, two estimates.
The actual
structure surface was divided into 220 facets,
80 on the inside and 80 on the outside walls with
60
on the top. The pressure gradient penetrated with attenuation roughly 0.5 to 1.0 r inside the well. Below that depth thepres-sure was roughly uniform. The small pressure gradient remaining there was probábly the result of using too coarse a mesh, but this did not affect over-all forces appreciably (by less than 1 percent). Assuming the well to be dead gave conservative estimates of horizontal force and overturning moment but the correct vertical force.
It is therefore recommended that if a well cannot be included in the structural modele it should be capped, the force and moment on the cap being subtracted at the end. The NPL program does this quite simply. Other types of indentation can be treated in a similar way, allowing for pressure variations on the bottom if this.is part of the structure. This procedure should normally providé a con-servative estimate of forces, but the moment must be treated with care. As noted, in Ref. 2, the overturning moment on a gravity structure with h/a= 0,8 is small as a result of the fine balance between forces on the base top and
sides. In the cases described here the
moment due tO side force predominates, so that an overestimate of horizontal force accompanies one of momênt. But if the base height is re-duced slightly, the top forces predominate. An ovérestimate of horizontal force may then reduce the overturning moment and give mis-leading results.
The physical effect of flow separation at the wêfl top probably makes the water in the well more dead than linear potentiaJ. flow theory predicts. But if the structure and well diameter are large, this is not expected to affect the over-all forces too much.
Moving Bodies
The NPL program was written with gravity structures in mind and at present works with fixed structures only. Recent developments in tension-stay, semisubmersible and spar-buoy-type platforms have raised questions concerning response to wave excitatiOn. The theoretical treatment of moving bodies is similar ta that of Í'ied bodies, invelving merely a change in
the body surface boi.mdary conditions. Under
the assumptions of lin?ar and harmonic re-sponse the body motion can be brOken down into oscillations in the six degrees of freedom, three of translation and three of rotation, as
described in Ref s, 15 (Section
19), 4.6
arid34.
Refs.
34
arid47
describe programs that solvethese component problems. They compute added mass arid damping. coefficients for bodies osciflating in. surge, sway, heave, roll, pitch and yaw in otherwise calm water, also the
exciting forces on the fixed body in waves. This capability will shortly be added to the NFL program.
Until then it is possible to estimate some of the coefficients. The Hasldnd relationshl° relate the forces on a fixed body lxi t1aves to
those on the same body oscillating in otherwise
still water. Thus for example, the principal
damping coefficients, according to Ref.
46,
Eq. 30, are proportional to the integrals overall incident wave directions of the squareC of corresponding exciting forces. This integra-tion is not practicable in general, but is simple if the body is añsymmetric abou the vertical axis, It then gives Newman's4 Eqs.
31
through33
for damping coefficients in surges heave and pitch in deep water orGarrison'
47 Eq. 44
for heave in shallow water.In many design situations the exciting wave is long compared with body dimensions. If
the response period is comparably long, there are several simplifications. First, according to Newman' s equations the damping coefficient is proportional to the cube of wave frequency and is therefOre small for long period
oscilla-tions. Second, the added mass fluid f9rces
acting on a body in motion depend only on the relative motion of the body and surrounding
fluid, If the body is small compared with
wavelength, it creates the same disturbance and experiences the same added mass forces whether it is fixed in waves and the surrounding fluid particles travel around elliptical Orbits or
itself travels around the same elliptical orbit at the same speed but in otherwisé still water. This means incidentally that, if the body excursions are small compared with local wave orbit diameters, the fluid forces are im-affected by body motion. To separate the co-efficients in heave, surge and sway, it is necessary to ook at the three òompänent
motions separately. Care is needed if the body is unsymmetric about the x = O or y = O plane because the horizontal acceleration phase of
the elliptical motion causes both horizontal and vertical forces, and similarly the vertical
phase. Many proposed structures fortunately
have double symmetry so that there are no surge/ sway/heave interactions. The separate fOrce components then give corresponding added mass coefficients, In cases where the body moves
care must be taken to use the full inertia force equations cited in Interpretation and Validity of Program, which includes the effect
of the acceleration of the actual mass of the body.
CONClUSIONS
1. Experimental measurements of over-all forces and moments on colunins gener11y agree well with the predictions of diffraction
theory, the measured forces being slightly
smaller.
This broadly confirms earlier
findings, but the eerimental results for the
square-section coluiris showed more scatter and
greater deviation from linear theory,
espe-ciVIy regarding the effect of wavebreaidng on
the vertical forces, as discussed in the next.
paragraph.
Measurements of the vertical force in
some cases tend to lie further below the
theoretical line than
inothers.
This is
thought to be associate4 with wavebrealdng
ob-served over the C luirai top.
In the case of the
circular columns, only the results for h/d =
0.9 are slightly affected.
For the square
columns where greater wavebrealdrig occurred
as may be eected, the effect is very much
stronger arid extends to h/d = 0.8 as well as
0.9.
Approidmate formulas are given for the
diffraction coefficients of circular columns
in quite long waves and deep water.
These
differ from the results of the full diffraction
analysis by less than about 5 percent.
40
The wavemaldng resistance of coluimis
in currents is much smaller than the drag.
it
is not thought worthwhile to include this.
effect in the NPL program.
The differences between linear and
Stokes V theory are small in tipicaJ. North Sea
design wave conditions, especially with regrd.
to inertia force.
More siificant is the
.differnce between integrating fôrces up to the
mean and actual free surfaces.
If wells inside gravity bases cannot
be includedin the full diffraction analysis,
they should be capped and corrected for later
on the assumption that the enclosed water is
dead.
This seems to give a conservative
esti-mate of fòrces but care is. needed in
interpreting the moment0
N0MECLATURE
a = column radius or
a,b = major arid minor haJ f-axes of ellipse
A = projected frontal area of body
c = current speed
Cd = drag coefficient
C ,C
y y
= diffraction coefficients for
hori-.
zontal force, vertcai force
nd
overturning moment, defined as
madmum total force or moment/
corresponding madmum
Froude-Krylov force or moment
Cm= mass coefficient
2 C= wave resistance/pAc
d = water depth
F=forée
= disturbance force
F= external force
e
Fk = Froude-Krylov force
F= Froude number
g = acceleration due to gravity
h = column height
H = wave height
k = wave number .2it/X or
k
C' Cm1, added mass coefficient
in review section
M = body mass
p = pressure
r = well radius
R = radial distance
t = time
T = wave period
u, .w = fluid velocity components. in x and
z directions
u, w = corresponding acceleration
conipo-nents
U.= fluid velocity
f luid acceleration
ACIÔWLEDGNTS
The authors wish tO acIthowledge their debt
to their colleagues who helped with this work,
especially to J. Osborne for conduct and
analysis of the experiments, and to H. Ritter,
R. A Browne and G. S. Smith for design of the
instrumentation.
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of Max'ine
Vehicles and Structures in Waves at
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Hogben, N., Osborne, J. and Standing, R.
G.:
"Tave Loading on OffshOre StruOtures
-Theory and Experiment," Proc., Symposium
on Ocean Engineering at the National
Physi-cal Lboratory, London, published by the
ROyal Inst. of Naval Architects (1974).
Hogben, N.:
"Fluid Loading o±i Offshàre
Structures, A State. of ArtAppraial: Wave
Loads," Maritime TechnOlogy Monograph No.
1, published by the Royal Institute of
Naval Architects (Nov. 1974).
aniilton, A.:
"A Low Load for Platforms,"
Financial Tithes, London (Nov. 1, 1974).
Anon.:
"Gravity Platforms:
Who is
Proposing What," New Civil :Hgineer
Speciàì Review on North Sea Oil (May
1974).
Paulling, J. R. and Horton, E. E.,:
"Analy-sis of the Tension Leg Platform,"
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Pet. Eng., J.
(Sept. 1971) 285-294.
Brogren, E.,.Soderstrom, J., Snider, R.
and Stèvens, J.:
"Field Data Recovery
System, Iazzn Dubal No. 3," Paper OTC
1943 presented at Sixth Offshore
Tech-nology Conference, Houston, May 6-8, 1974.
Marion, H. A.:
"Ekofisk Storage Tank,"
Royal Inst. of Naval Arçhitects Symposium
on Ocean Engineering, Nov. '1974.
'9.'
P. E.;Tòwnshend, M. A.:
"Offshore Storage
and Tanker Loading," Royal Inst. of Naval
Architects Symposium on Ocean Engineering,
Nov. 1974.
Paulhirg, J. R.:
"Elastic Response of
Stable Platform Structures to Wave
Loading," Prc., International Sympo siuin
on Dynamics of 'Marine Véhicles and
Struc-tures in Waves at University College
London, published by the Inst. of
Mech-anical Engineers (April 1974).
Hooft, J. P.:
"A Mathematical Method of
Determining Hydrodynamically Induced
Forces on a Semi Submersible," Trans.
SNAME (Nov. 1971).
Havelock, T.H.:
"The Pressure of Water
Waves Upon a Fixed Obstacle,"
Roy.
Soc. A-963 (1940)
.John, F.:
"On the Motion of Floating
Bodies Pért II," Ccrnim. Pure and Applied
Maths (1950)
.MacCamy, R. C. and Fuchs, R. A.:
"WaveForces on Piles:
A Diffraction Theory,"
Beach Erosion Board Technical Memorandum
No. 69 (1954).
Wehausen, J. V. and Laitone, E. V.:
"Surface Waves," Encyclopaedia of Physics,
Springer, Brlin (1960).
Hess, J. L. and Smith, A.M.0.:
"Calcu-lation of Potential Flow About Arbitrary
Bodies," Progress in Aeronautical
Sciences (1967)
.Garrison, C. J. and Chow, P. Y.:
"WaveForces or Submerged Bodies," ASCE
Water-ways and Harbors Div. (1972)
2.
Morison, J. R., O'Brien, M. P., Johnson,
J. W. and Schaaf, S. A.:
"The Force
Exerted by Surface Waves on Piles,"
Trans., AINE (1950) .12.
Gran, S.:
"Wave Forces on Submerged
Cylinders," Paper OTC 1817 presented at
Fifth 'Offshore Technology Conference,
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Chalabarti, S.:
"Wave Forces on
Sub-merged Objeçts of Symmetry," ASCE
Water-ways and Harbors Div. (1972)
2.
Garrison, D. J. and Snider, R. H.:
"WaveForces 0±1 Large Submerged Tanks," Texas
AßeN U. , Sea Grant Publication No. 210
COE Report No. 117, 1970.
O'Brien, M. P. and Morison, J. R.
"The
Fôrces Exerted by Waves on Objects," Trans,
Amer. Geophys.,Union (Feb. 1952)
, No. L
Shank, G E. thd Herbich, J. B. :.
"Forces
Due to Waves on Submerged Structures,"
Texas MN U. COE Report No. 123, May 1970.
Schiller, F. C.:
"Wave Forces on a
Sub-merged Horizontal' Cylinder " MS thesis,
Naval Postgraduate School, Monterey,
Calif.,Report No. AD 727 691 (June 1971).
Brater, E. F., McNown,J. S. and Stair,
L. D. :
"Wave Forceé on Subnierged
Struc-tures," J. of the Hydraulics Div., ASCE
(Nov. '1958)
Nó. HY6.
'Jen, Y.:
"Wavé Forces on Circülar
Cylin-drical Piles Used in 'Coastal Structures,"
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Lebreton, J. C. and Cormault, P.:
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Some Theoretical and Experimental
Con-siderations," Proc. Symposium, "Research
on Wave Action," Deift (1969) J.
Van Oortmerssen, G. :
"Some Aspects of
Very Large Offshore Structures," Ninth ONR
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"Wave Action on Large
Off-shore Structures,," Proc., Inst. of Civil
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Struc-tures, London (Oct. 1974).
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Mers en Profondeur Constante ou
DScroissante," Annales des Ponts et
Chaussees (1944).
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"A Theory, of the
Origin of Micro seisms," PhIl. Trans. A243
(1950).
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des Mouvements d'un Navire ou d'une
Plateforme Arnarre dans la Houle," La
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, 379-389.
Faltinsen, O. M. and Michelsen, F. C.:
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Zero Froude Number," International
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"Gross
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Cylinder - Theory and Experiment," Paper
OTC 1818 presented at Fifth Offshore
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N. HOGBand R. G. STA1DING
L2 3EXFERIENCE IN COUTING WAITE LOADS ON LARGE BODIES OTC
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TABLE i - COARISON BETWEEN COÌ.PUTED DIFFRACTION COEFFICIETS FOR CIRCULAR CYLITDERS Ch Ci,, C : DIFFRACTION TIORY AND APPROXIMATE FORMULA
.L'kACTÏON
THEORY FROM REF. 2
APPROXThLATE FORMULA ka
h/2a
h/d
Ch C C Ch Cv C0.1
0.75
0.15
1.70
1.01
1.78
1.68
1.01
1.87
0.75
0.3
1.70
1.011.78
1.68
1.01
1.87
1.75
0.7
1.89
1.02
1.86
1.90
1.01
1.87
0.2
0.25
0.1
1.44
1.01
0.93
1.47
1.01
.1.83
0.2
1.60
.1.02
1.92
1.59
1.01
1.83
0.5
0.4
1.63
1.02
1.94
1.59
1.01
1.83
0.75
0.3
1.70
1.03
1.78
1.67
1.02
1.83
0.75
0.6
1.76
1.Ö3
1.83
1.67
1.02
1.83
i..O0.8
1.87
1.06
1.89
1.74
1.03
1.83
1.25
0.5
1.81
1.05
1.81
1.80
1.04
1.83
1.75
0.44
1.89
1,08
1.86
1.89
1.05
1.83
1.75
0.7
1.89
1.08
1.86
1.89
1.05
1.83
2.25
0.56
1.89
1.09
1.85
1.91
1.07
1.83.
?.25
0.9
1.98
1.15
1.94
1.97
1.07
1.83
0.5
.25
0.1:1.42
1.04
0.98
1.44
1.05
1.73
0.5
0.2
1.57
1.10
1.86
1.55
loO.91.73
0.5
0.4
1.60
1.12
1.89
1.55
1.09
1.73
0.75
0.3
.1.66
1.15
1.72
1.63
1.14
1.73
0.75
0.6
1.71
1.20
1.78
1.63
1.14
1.73
1.0
0.8
1.85
1.42
1.85
1.69
1.19
1.73
1.25
0.5
1.74
1.23
1.72
1.75
1.23
1.73
1.75
044
1.78
1.28
1.74
1.84
1.25
1.7.31.75
0.7
1.78
1.28
1.74
1.84
1.25
1.73
2.25
0.56
1.80
1.27
1.74
1.91
1.25
1.73
2.25
0.9
1.90
1.63
1.86
1.91
1.25
1.73
1.0
0.251
0.2
1.34
1 17.1.17
1.33
1.18
1.55
0.5
0.4
1.44
1.33
1.54
.1.42
.1.37
1.55
0.75
0.3
1.54
1.43
1.54
1.48
1.50
1.55
0.75
0.6
1.49
1.43
1.47
1.48
1.50
1.55
1.0
0.4
1.58
.1.48
1.54
1.53
1.50
1.55
1.0
0.8
154
1.57
1.49
1.53
1.50
1.55
1.25
0.5
1.59
1.49
1.54
1.57
1.57
1.55
1.5
043
1.62
.1.52
1.56
1.60
1.50
1.55
1.5
0.6
1.59.
1.48
.1.53
1.60
1.50
1.55
.1.75
Ó.5
1.63.
1.53
.1.56
1.63
1.50
1.55
1.75
0.7
1.58
1.46
1.53
1.63
1.50
1.55
STILL WATER LEVEL
ELEVATION
Fig. i - Series of circular and square section columns of varying height.
o
c)
r
PLAN:
'j
Si
S
S
S
t
Fig. 2a - Dynamometer and circular column
(h/d
0.7) before mounting.
WATE H O9d SURFACE DEPTH di
O7 ¿ 08 ¿ PIERCING TAN K BOTTOI.Is
j
I
test
column
Fig. 2b
- Ctaway
view of te;st
co I ümn mounted on
dynamometer.
b) 2 - component
horizontal
force
flexure
(upper)
f) 2-component
horizontal
force
flexure
(lower)
strain
gauges
strain
gaugesStrain
gauges
a) vertical
force
flexure
c) spokes
transmitting
horizontal
force
e)'floatiflg'
cylinder
g) spokes
transmitting
horizontal
f orceh) base
plate
Fig. 2c - Di.agirammattc sketch of
HORîZOS1AL FOUC COPUTED
k.
VERTICAL FORCE
SPOTS DENOTE MEASURESIENTS USING STRAIN GAUGE O H/. - 033
DYNAIIjOMETER- - IN WAVES OF VARIOUS HEISS 0 022
- A- 0.17 V 0.11
hid - ös
04 IO 15 0 0.5 1-0 1.5 HORIZONTAL FORCEh/d
og
MOMENT MOM EÑ TSPOT! DENOTE MEASUREMENTS USINO STRAIN GAUGE .0 H/P - 0.33
ZIVNAMOMEIER IS WAVES OF VARIOUS HEIGHTS 0 022
- £ 0.17
V DII
SPOTS DENOTE MEASUREMENTS O 4/. - O-33 USING STRAIN GAUGE 0 022
DVNAMOMETER IN WAVES .0 0-1
OF VARIOUS HEIGHTS V 0.11
112 99 H
2.
SPOTS DENOTE MEASUREMENTS USING STRAIN GAUGE DVNAMOMETER IN WAVES OF VARIOUS HEIGHTS
COMPUTED
2 COMPUTED
k. IO I
h/d
-07-HORIZONTAL FORCE - VERTICAL FORCE
COMPUTED
-s-HORIZONTAL FORCE
COU UT E D
h/d
08
SPOTS DENOTE MEASUREMENTS USING STRAIN GAUGE O H/ -0.23
DVNAMOMETER IN WAVES OF VARIOUS HEIGHTS 0 022
6 0.17 V 0.51
HORIZONTAL FORCE VERTICAL FORCE MOMENT
e COMPUTES
--/2pHPd I I I I IO IS 0 05 k 1.0 1.5h/d
09
SPOTS DENOTE MEASUREMENTS USING STRAIN SAUSE DYNAMOMETER IS WAVES 0E VARIOUS HEIGHTS I
MOM E NT
O
0.0
Fig. 3 Comparison of computed and measured force.s and moments on vertical columns.
o R1N-0-33
O G-22
A 07
V Oli
CIRCULAR SECTION
SQUARE SECTION
SPOTS DENOTE MEASUREMENTS U5ING STRAIN GAUGE o H/H 033 ETNAMOMETER IN WAVES OF VARIOUS HEIGHTS 0 022
L 017
V 0-It
SPOTS DENOTE MEASUREMENTS USING STRAIN GAUGE O lI/ooS3
DYNAMOMETER IN WAVES OF VARIOUS HEIGHTS o 022
5.17
V OIl
SURFACE PIERCING SURFACE PIERCING
HORIZONTAL FORCE VERTICAL FORCE
e
0 o
k o ES
VERTICAL FORCE MOUE NT
1-!
Cw
...-.--
'---'- .- -
--
-
__*__ ,/
%\
-2
Fig. 4- Effect of diffraction on the wave
profile over a square section colymn (see fig.
h/d
0.9, ka
I .0).Phase= 2.22 RAD with
maximum total downward force.
I4
12
19
08
O4
02
TOTAL WAVE INCIDENT AND SCATTERED 2,e7TOTAL
WAVE AMPLITUDEINCIDENT WAVE THEORY
k
¡'EXPERIMENT
/5
1'
\
THEORY gi (CIRCLE)
I I - I---O--- MEASURED WAVE PATTERN
RESISTANCE ASSUMINGEFFECTIVE E = O'2
2b
I. i= b/a
(_ . I- -i
2a
J
0.3
04. O5
06
O7
08
O9
. I-213
IFn.
Fig. 5
- Comparison of theory. with experiment
-10
O 11/4
/2
311/4211 (t/r._x,À)
Fig..6- Linear änd Stokes V
rófuIésofwäve
elevation, maximuîi acóeleration añd velocity
coth-ponents.
. .050
00.25
wo
-O25Fig; 7- Linear
force and overturn
.IL,/9 O
2
2z
w4
w..
.o
11/2 :11/2 /4050
025
I-z
wo
2 4.025
-04
-02
p pi-o
oW4
W2and Stokes V, drag and i.hertia,
ng moment on a sLendercoiumn.
H/9T2
0015
M/d =02
WI WI / !/2 9H-02
O- LINEAR TO Z-0
-- STOKES V TO Z=0
STOKES V TO Z-U.ILLI/I/2 9Ho
02
04.
Z. O-4-
FORCE H IL ea DI
O-2o
l-5
1-0
o-N(L 05
O O-06-g: O-04O-O2-00
0-2 0-4 0-608
OVERTURNING I I I d MOMENTrfa
02
0-4
0-6 0-80-5
i::T
zoo;
-I I Ir 0'r/a
i 0-2 0-4 0-608
MODEL WITH WELL
-- FORCE ON CAPPED
MODEL - FORCE ON CAP FORCE ON CAPPED MODEL X VOLUME RATIO. PLANd/a = 3
h/a = O-8
Fig.
8 -
Estimates of linear forces and overturning moment on circular bases withcentral wells.
0-2 0-4 O-6
08
0-2
0-4.
06
0-8(b)