heat transfer from a cylinder in an acoustic standing wave
TRANSCRIPT
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Heat transfer from a cylinder in an acoustic standing wave
George Mozurkewich
PhysicsDepartment,Ford Motor CompanyResearchLaboratory,Mail Drop 3028, P.O. Box 2053,
Dearborn, Michigan 48121-2053
(Received 4 February1995;acceptedor publication 4 May 1995)
Heat transferwas measured rom wires of various diameters ocated at a velocity antinode n an
acoustic tandingwave.A transientmethodwasused, n which the rate of heat ransferwas deduced
from the rate of changeof temperature fter heatingwas turned off. For fixed wire diameterand
acoustic requency,he dimensionlesseat-transfer oefficient Nusseltnumber)Nu showsa
distinctive variation with acousticamplitude. At high amplitude, Nu follows the well-known,
steady-flow, orced-convection orrelation, ime averagedover an acousticcycle, while at low
amplitude,Nu has a constant alue determined y naturalconvection. he transitionbetween hese
regimes,which occurs ather abruptlywhen the streamingReynoldsnumber (basedon wire
diameterand acoustic elocityamplitude) quals88, is discussedn terms of a heat-transfer
bottleneck hat s openedby acoustic treaming. n empiricalcorrelation s presented. pplicability
to heat exchangersor thermoacoustic eat engines s considered. 1995 AcousticalSocietyof
America.
PACS numbers: 43.35.Ty, 43.35.Ud, 43.25.Nm
INTRODUCTION
Thermoacoustic ngines or cooling and for soundgen-
eration have recently become a subject of technological
interest.In somenstances,hepracticalityf thermoacous-
tic enginesdependson efficient operation.A major factor
contributing o overall efficiency s the effectiveness f heat
transferbetween the soundwave and the heat exchangers.
Optimal designwill dependon an understanding f the me-
chanicsof the heat-transfer rocess.
Thermoacoustic eat exchangers an be broadly classi-
fied into those involving internal flow in ducts or porous
geometries nd those nvolving external low aroundobjects
that are genericallycylinders.The first class s represented
by parallel-plateand honeycomb tructures hile the second
includes wire screens and reticulated foam. Work in this
laboratoryhas employedscreens nd foam and has assumed,
for designpurposes, hat the heat-transfer oefficientsmay
be obtained rom well-known, steady-flowcorrelations or
cylinders.The present nvestigation xplores he validity of
this assumptionor acoustic low aroundcylinders.
The influence of sound or vibration on heat transfer is a
problem that has generatedconsiderable xperimentaland
theoretical nterest.A valuable, early review was given by
Richardson,who, ettingside uoyancy,appedheprob-
lem in termsof two parameters, amely, he ratios of acous-
tic displacementor vibration)amplitude l and of viscous
diffusion ength r5 to cylinder diameterd. To avoid the se-
rious complicationof boundary-layerseparation,most theo-
retical treatments ave beenrestricted o the small-amplitude
limit, xi/d•l. Those investigationshave identified the
steadylow nown sacoustictreaming'4 s hemechanism
that cartes heat away from the vicinity of the cylinder, as
suggestedn early xperimentalork.-7Mostexperiments
with stationary ylinders n acoustic ields or with vibrating
cylinders n nominally stationary luids have been performed
in this imit. In the opposite,arge-amplitudeimit,heat
transferhas been ascribed o "convectionby time-average
steady-flowequivalent."The present nvestigationwill sug-
gest that this ascription s incomplete. Buoyancy effects,
whichgreatly omplicateheanalysis,anbe neglected'9
whenGr/Re is small nough,s n this nvestigation.Gr
and Re are the Grashofand Reynolds umbers; eebelow.)
For more recentwork, see Davidsonø and Peterkaand
Richardson. M nother review that shouldbe of interest for
the case of internal-flow heat transfer has recently
appeared.2
Thermoacoustic nginesoperate on the borderlinesbe-
tween hese imits. Because he oscillating luid conveysheat
betweenheheatexchangernd hermoacoustictack,the
longitudinal dimensionof the heat-exchange tructuremust
be less than or roughly equal to the acousticdisplacement.
Hence, for external low aroundwire screens r through e-
ticulated oams,x •/d•> 1. Good thermoacoustic esignof the
stack equires ransverse imensions f the pores o be a few
times rSv. ssuming hat the heat-exchangetructure oesnot
have a grosslydifferentscale, rS,/d-1.
This investigationwas undertaken o characterizeheat
transfer rom acoustic low aroundcylinders n this theoreti-
cally awkward regime that is also not well exploredexperi-
mentally.The intent was to producea correlation hat could
be applied o the designof thermoacousticeat exchangers.
The correlation hat was obtained s not directly applicable o
thermoacoustic evices,however, because he geometry of
this experimentdiffers in two important respects rom the
physical situationrelevant to thermoacoustic ngines with
external-flowheat exchangers. irst, in the presentcase the
cylinder s isolated,while in engines he heat exchangers re
adjacent o a porousbody, the stack. Second,any practical
heat exchangermust consistof a plurality of cylinders hat
would interactwith eachother n a complexway. Hence this
investigation epresents nly a first step toward solving the
practicalproblem.
2209 J. Acoust.Soc. Am. 98 (4), October 1995 0001-4966/95/98(4)/2209/8/$6.00 ¸ 1995 AcousticalSocietyof America 2209
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8/20/2019 Heat transfer from a cylinder in an acoustic standing wave
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lb)
Moveablelunger
•ne
(c)'
Loudspeaker
FIG. 1. (a) Circuit or measuringesistancen presence f biascurrent. b)
Acousticapparatus, howing esonance ube with loudspeaker,moveable
plungerwith microphone,ndwire under est. c) Detailof wire mountedn
Teflon holder with voltageprobes.
I. EXPERIMENTAL METHOD
The experiment onsisted f placinga heatedcylindrical
wire at a velocity antinodeof a standingacousticwave and
measuring he rate of transferof heat from the wire to the
acoustic medium. This section describes the methods of mea-
suringheat transferand of applying he standingwave.
The cylindrical wire servedas heater and thermometer.
Jouleheatingwas obtainedby passing large current rom a
dc source hrough the wire. Temperaturechangeswere de-
duced from a four-probemeasurement f the wire's resis-
tanceusinga smallalternatingurrent 1 mA at 16 kHz) and
a lock-in amplifier Fig. l(a)]. Titaniumand rheniumwere
chosenas wire materialsbecause hey have relatively large
yet strongly temperature-dependentlectrical resistivities.
Diametersranged rom 0.125 to 2.0 mm.
The heat-transfer coefficient h was deduced from the
decay of the wire temperatureTw toward ambient T O after
turningoff the Jouleheatingwhile maintaining ixed acoustic
amplitude.Assuming hat the temperaturenside the wire is
radially uniform and that the ends are maintained at fixed
temperature,Tw is only a functionof the axial coordinate .
Let the wire have length 2L along z between its voltage
contacts,diameterd, perimeter I=vrd, and cross-sectional
areaA = vrd2/4, nd et thematerial ave hermal onductiv-
ity ks specificheat cs, densityPs, and thermaldiffusivity
xs=ks/psc Thedecay beys3
o2 w o( w to)
ksA 9z-hII(Tw-Tø)=PscsA9t ' (1)
The Appendixpresentshe solution.To leadingorder,which
is good enough for all practical purposes, he relation be-
tween h and time constant r is
(2)
The first term arises rom heat lost radially through he cy-
lindrical surface,and the second rom heat flowing parallel
to the cylindricalaxis. The second erm usuallyamounted o
a smallcorrection
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being a velocity node and the driver roughly an antinode, he
tube then contained3/4 wavelengths,with a velocity antin-
ode at the wire location. The effect of the driver location's
not being a perfectantinode ouldbe compensated y replac-
ing the wire by a second1/2-in. microphoneand adjusting
frequencyand plungerposition o obtain a pressure ode at
the wire location.Higher frequencies ould be obtainednear
odd multiplesof 141 Hz, or, by moving he plunger,at vari-
ous other requencies. he highest requencyusedwas 2391
Hz.
The velocity amplitudeat the wire, u , was calculated
from the pressure mplitudeat the plunger,P l, according o
u =Pl/pgC, wherepg andc arethe density ndspeed f
sound in the gas. At 141 Hz, distortion of the sinusoidal
wave form at the plungerwas insignificantup to the largest
amplitudeattempted,correspondingo a 22-m/s peak. Dis-
tortionwas greaterat higher requencies. or example,many
experiments were performed at 840 Hz where second-
harmonicdistortionas large as p2/pl=O.15 was observed.
However, the distance between the wire location and the
plungerwas always an even numberof quarterwavelengths
for even harmonics.Therefore u2-0 at the wire location,
leavingonly higherharmonics hat were correspondingly e-
pressed n magnitude.
II. RESULTS
Resultsrepresentedn dimensionlessorm. 3Let the
gashave hermal onductivityg, density g,heatcapacity
Cp, and hermal iffusivityKg=kg/pgCp. eat transfers
characterized y the Nusselt number
Nu=hd/kg (3)
Velocity s characterized y a ReynoldsnumberRe , based
on acoustic elocity amplitudeand wire diameter:
Rel=Uld/V, (4)
where v is the kinematicviscosityof the gas.For the purpose
of describingnatural convection, he temperature ifference
is characterized y the product of the Grashof and Prandtl
numbers,
Gr=d3/• g(Tw- To)/V , (5)
Pr= v/Kg. (6)
Here,/• is the gas's hermal expansivity, nd g is the accel-
erationdue to gravity. The productGrPr is called he Ray-
leigh number.)For forcedconvectionn a steady low, Re
and Pr suffice to determineNu. In an oscillating low, one
more parameter must be introduced o account or the fre-
quency of flow eversals.DefiningheStokes epth, r
viscous diffusion length during an acoustic period, by
8•,=v/rrf)1/2Swift'sotationl),his dditionalarameters
taken to be the ratio 6v/d.
The experimentalmethodwas testedby measuring atu-
ral convection i.e., without sound) rom a 0.25-mm Re wire
overa rangeof temperatureifference w- To. ResultsFig.
2) areconsistentithpublishedecommendedalues.7 he
figure also shows hat heat transfer n the presence f intense
sound s independent f temperature ifference.
10
,1 i i i i i i i i
0.001 0.01 0.1 1
GrPr
FIG. 2. Nu vs GrPr for 0.25-mm rheniumwire. Open circles:natural con-
vectionmeasurementsno soundwave); he ine s a smooth urve hrough
recommendedalues seeRef. 17). Filled circles:measurementsith arge
soundwave; line is a guide for the eye.
The characteristic variation of heat transfer with acoustic
amplitude xhibits hree egimes Fig. 3). For smallampli-
tude, heat transfer s independent f amplitudeand equal to
the free-convection alue.For large amplitude,Nu is propor-
tional o Re•/2, eminiscentf thecorrelationor laminar
steadylow. 8The ransitionetweenheseimiting ehav-
iors is fairly abrupt n that, over a substantialangeof Re1
Nu is smaller han would be expected rom the square-root
variation.This behavior n the transition egion suggestshe
existenceof a bottleneck n the pathway for heat removal.
With increasing requency, he transitionregime moves to-
ward argerRe1 (Fig. 4).
The square-rootbehavior at large Re 1 has been ex-
lO
o vertical •J•
,_, 1/2 -•
............•e ..../
..-
ß
ß
..
,..
, •. ...... i ........ i , , , , •1
1 o 1 oo 1 ooo
Re
1
FIG. 3. Nusseltnumberversus coustic eynolds umberat fixed requency
(142 Hz) for 3/4-mm Ti wire. Resultsare shown or horizontaland vertical
sound ropagation.ymbols: ata.Solid ines:correspondingits o Eq. (8).
Dotted ine: Eq. (7).
2211 J. Acoust. Soc. Am., Vol. 98, No. 4, October 1995 George Mozurkewich'Heat transfer n an acousticstandingwave 2211
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lO
, i i i
014,5z
• 842
, i i , i , , i
10 100 1000
Re
FIG. 4. Nu vs Rel at three requenciesor 3/4-mm Ti wire. Lines are fits to
Eq. (8). With increasingrequency,he transitionrom small o largeNu
moves oward larger Rel.
plainedas "convectionby time-average teady-flow quiva-
lent," as demonstrated y an early experimentusinga heated
cylindern water.9•ukauskas8recommendsu=0.51
Prø'37 e '5 or a cylindern steady rossflow,or 40
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TABLE I. Experimentalesults. irst threecolumns escribe xperimental onditions. ext threecolumnsist
parametersbtainedrom its o Eq. (8). Lastcolumn ivesexpectedalues f Nuna(seeRef. 17)'
Wire f (Hz) •,,/d K Re•it Nuna Nh'thy
' •*nat
1/8-mm Re 145 1.440 0.280 8.45 0.46 - 0.48
841 0.599 0.255 19.0 0.42
1/4-mm Re 145 0.722 0.368 25.6 0.65 0.60
840 0.299 0.271 29.6 0.60
3/4-mm Ti 143 0.238 0.327 44.2 0.90 0.95
278 0.171 0.353 60.2 0.88
422 0.138 0.319 69.7 0.91
842 0.095 0.378 141.0 0.91
2391 0.057 0.270 186.0 0.98
2-mm Ti 144 0.090 0.425 214.0 1.16 1.50
840 0.038 0.425 517.0 1.11
One experimentwas performedwith a mixture of 20
mol % argon in helium at approximately1 bar, using the
0.75-mm Ti wire at 230 Hz. Nu vs Re• showed the same
qualitativeeaturesndwas it to the same orm,yielding
Nunat=0.41,=0.27,andRe•it:34.7.
In order o illustrate he qualityof the fit, all data (ex-
cluding he He-Ar mixture)are plottedon a singlecorrela-
tion curve n Fig. 6. These data cover a broad range of pa-
rameters, including 1
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fore the parcelreturns o the vicinity of the wire. Yet a fourth
possiblemechanisms vortex shedding, s the vorticescarry
energy. Whatever mechanism s effective, the important
point s that the rate limiting step s the transferof heat from
thewire nto hemoving as,which ccountsor heRe /2
dependence.Thereafter, sufficient time elapses for the
"other" mechanism o remove hat heat from the gas before
the gas returns o the wire's vicinity. If its effectiveness e-
pends n Re morestronglyhanRe /2, then he other
mechanismwould becomerate limiting below some ower
value of Re1.
A clue to the identity of the mechanism hat impedes
forced-convectioneat transferat smallerRe1 couldbe pro-
vided y heobservednverseroportionalityetweene•it
and 6v/d. It is important o realize that the set of dimension-
lessnumbers hat was chosen or this analysis orms a com-
pleteset within he assumptionf incompressiblelow near
the wire): any otherdimensionlessumber hatcouldpossi-
bly be physically elevant o the presentproblem Strouhal
number, roudenumber, r whatever) an be formedby an
appropriate roductof membersof the chosenset. By sub-
stituting q. (9) into Eq. (8), one inds hat he parametriza-
tion becomesparticularly simple in terms of the product
Re1 6v/d, a combination hich suggestscoustic treaming,
as will now be shown.
Acoustictreamingnducedy thewire Ms a likely
candidate or the bottleneckmechanism.n the perturbative
limit, '22he haracteristictreamingelocitys nthevicin-
ityof hewire sus- u•/ood,orwhich streamingeynolds
number can be defined: •
Res=
l= 2
:• d ' (10)
to 1.4d. Buoyancy does not seem to be involved because
Re•it swellcorrelatedo 6•/d withoutllusiono empera-
ture difference. his might be regarded s a weak argument
because he temperature ifferencewas not varied widely
and because the orientation of the tube showed some effect.
Nevertheless, ven if buoyancyplays somesubsidiary ole,
thepredominantependencef Re•iton •/d demandsn-
other interpretation.Thermal diffusion does not seem to be
involvedbecause, y the following argument, his also m-
plies x 1-d for the critical case.Let L be the lengthof the
wire,Tg the emperaturef a typicalgasparcel, ndb the
thickness f the thermal ayer adjacent o the wire. In order
of magnitude,7 he ateat which e//t s removedrom he
wire s kgLd(Tw-Tg)/b,and he nteractionime s d/u1.
Thus the total amount of heat abstracted is
kgLd[Tw- Tg)/b d/u1- Similarly,he otalheat ransferred
from the parcel to its cooler surroundings is
kgLXl[(Tg-To)/b]Xl/U . The latter expressionssumes
that the distance ver which he heatmustdiffuse s compa-
rable to b, which follows from conservation f mass.By
equatinghese xpressionsndsolvingorTg, one indshat
the transitionromcoolgas o hot gas,Tg=(Tw- T0)/2,
occurswhen x 1-- d.
Results or the helium-argon mixture (Pr=0.40) are
more or lessconsistent ith those or air (Pr=0.71). Exten-
sive experimentswith air alone are, of course,unable o dis-
cern nydependencef K, Re•it,orNunaonPr; hechosen
parameterization,q. (8), assumes forced-convectione-
pendenceroportionalo Prø'37. hereashemixture'salue
K=0.27 falls just one standard eviation rom the average
for air (Table ), thatassumptioneemso be valid.As for the
transition,he mixture'sxperimentalalue,Re•rit=34.7,
falls a little more hanone standard eviationbelow he pre-
dictedvalueof 39.2_+3.9 ased n Eq. (9). However,onecanCombining he last form with Eq. (9), one finds that the
transitions characterizedyRes=88.his impleesult generaten nfiniteet fexpressionshat re quivalentn
air to Eq. (9), suchas
suggestshat streamingplays a key role in breaking the
bottleneck.
Acoustic streaming s a physicallyreasonablemecha-
nism becausehe consequentteady low is capableof car-
rying heat to greatdistancesrom the wire. Yet the physical
significancef Res=88 (or of theequivalentormx1=6.6
is notclear.t maybeworth otinghatBertelsen3observed
an nstabilityearRes= 00of thestreaminget24 manating
from a vibrating ylinder. he fact thatRes hasbeendefined
usinga perturbativeorm for the streaming elocity aisesa
concern. The ratio of streaming o acousticvelocity is
us/u 1--Res/Re1,hich quals 8/Re•itat the ransitional
value of Re1. Thus n theseexperimentshe calculated alue
of Us/U1 at the transition angedup to -10, where he per-
turbativereatmentails?Furthermore,t seemsmplausible
on physicalgroundshat us could substantiallyxceedu
Nevertheless, the data indicate that the behavior is controlled
by the numerical alueof Res as defined n Eq. (10).
To strengthenhe argument hat streamings important,
an attemptwill be madehere o systematicallyliminateal-
ternativemechanisms. ortexshedding oesnot seem o be
involvedbecause oundary-layereparation ecomes con-
cernwhen •-d, 26 n conflict ith heempiricalesulthat
the ransition ccurs hen 1--8• for 8v angingr6m0.04d
=(15.8-+1.6)
(11)
eachof whicha,rnountso a differentassumptionbout hePr
dependencef Re•it.Themixture'sxperimentalaluealls
nearly two standarddeviationsabove the predictedvalue
29.3-+2.9 basedon Eq. (11). Therefore,of these wo forms
the one basedon 6•/d seems o be preferred,although he
presentdata permit some ntermediatePr dependence,ike
Re•ritøc[(/• v)1/2/d]-1.
The dependencef heat ransfer n the magnitude f Res
that s found n theseexperiments eems o be unanticipated.
Richardson'salculations,applicable hen (5•/d0.3, wheremost
of thepresentmeasurementsall. The space,of l/d vs 8v/d
is shown n Fig. 7 along with the region occupiedby the
presentexperiments nd variousborderlines nticipated y
Richardson.Thesolidineshows es=88.t is apparent
that the experimental ehaviorchangesqualitativelywhere
no changewas expected,and that no qualitativechange s
observedwherechangeswere expected.
2214 J. Acoust. Soc. Am., Vol. 98, No. 4, October 1995.
George Mozurkewich: eat transfer n an acoustic tandingwave 2214
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103
2
1
10 0
-1
-2
10 3 ........ i o .I .,I
10-3 10-2 10-• 10 0 10 •
FIG. 7. Coordinate pace s dividedup into various egions dashedines)
by RichardsonseeRef. 2): convection y inneracoustic treamingA), by
outeracoustic treamingB), by time-average teady-flow quivalent C),
and rivial effects D). Circles:ocations f datapoints.Solid ine: Res=88.
IV. CONCLUSION
Heat transfer rom a heatedwire at a velocity antinode
in an acoustic standingwave was found to fall into three
regimes. For small acousticvelocity, free convectiondomi-
nates. For large acousticvelocity, the heat transfer s deter-
mined by its time-average teady-flow quivalent. n this re-
gime, the rate determiningprocess s the abstraction f heat
from the wire into adjacentparcelsof flowing gas; whatever
the process hat eventually carries the heat to infinity, it is
fast enough that it does not limit the overall heat-transfer
rate. The transitionbetween he two limiting regimesoccurs
for Res=88. In the vicinity of this Res that other process,
which appears o be acousticstreaming, s the rate limiting
step.
In this experiment, the wire interacted hermally only
with gas in an open tube, while in thermoacoustic ngines,
the heat exchangers re located mmediately adjacent o the
stack. From the standpointof thermoacoustic pplications,
the most importantpracticalquestion nvolves the effect of
the proximity of the stack. Provided that the gas parcels
move far enough o interactwith the stack, he stack s pre-
sumablycapableof transferring eat to or from the parcelsas
necessary.f so, the presenceof the stack would open the
bottleneck n the intermediate egime, and the heat-transfer
coefficientwould increase o the value expected rom time-
average steady-flow equivalent. Therefore, provided that
x• >>d, the relevant heat-transfer ate could presumablybe
estimatedrom Eq. (7).
Several directions or further investigationmay be sug-
gested. All these measurementswere performed with the
wire located at a velocity antinode. By locating the wire
elsewhere,one could explore the heat-transfer ffect of the
streamingpattern induced by the resonant ube's walls, as
well as any possible nfluenceof a superimposed scillatory
pressure. n this work only one gas mixture was used.More
extensive measurements with mixtures are needed to sub-
stantiatehedependencef •' crit
•e• on Pr. While theseexperi-
ments were motivated by a practical problem in thermoa-
coustics, the results are not directly applicable there.
Measurementsare needed with more realistic geometries,
suchas wire screens, nd n the proximity of someheat sink,
preferably a thermoacoustic tack.
ACKNOWLEDGMENTS
The author is grateful to L. C. Davis, D. F. Gaitan, A.
Gopinath,S. R. Murrell, W. L. Nyborg, V. W. Sparrow,and P.
J. Westervelt or helpful discussions nd communications.
APPENDIX
This section resentshe solution o Eq. (1), which de-
scribes he axial temperature istribution n a cylinder sub-
ject to convectiveheat transport hrough ts cylindrical sur-
face. Based on the argument in the text, the radial
temperaturevariation within the cylinder is assumednegli-
gible; the only relevantcoordinates z, which lies along the
cylinder axis. The wire initially attainsa steady emperature
distributionby being subjected o steadyJoule heating, and
the transientbehavior hat ensuesafter turning off the Joule
heating s to be determined.The wire's ends at z =- L will
be assumedo be maintained t temperature •,.
Effectsof Jouleheatingq* per unit volumemay be in-
cluded y adding * to the eft-hand ideof Eq. (1). Defining
O(z,t) rw(z,t)-r 0 andX-(ksA/hlI)u2, t becomes
092 1 1 090 q*
•z2 h20- . (A1)
s 8t ks
Upon omitting the first term on the right-hand side and de-
finingU=q*X2/ks, hesteady-stateolutions easilyound
to be
cosh(z/X)
O(z,O)--(U+ o-rb) osh(L/X) (A2)
The subsequent ransient solution was found by Laplace
transformation. The result is
cosh(z/X)
O(z,t)=(rbTo) osh(L/k)
n=O ½/'(/•-21-)q-½/.2(/•-21_)2(•k2/L)
Xexp Ks + L2 t . (A3)
The reader may confirm that it satisfiesEq. (A1) (with
q*=0), the boundary onditions, nd the initial condition.
[For the initial condition, onsiderhe Fourier-seriesepre-
sentation f Eq. (A2) on an intervalof length4L.] The ex-
periment measuresnot the temperaturedistributionbut the
resistance. aking the resistanceo be linear in T, its variable
part R(t) is proportionalo the spatial ntegralof Eq. (A3)
from -L to L. Thus
2215 J. Acoust. Soc. Am., Vol. 98, No. 4, October 1995 George Mozurkewich: Heat transfer in an acoustic standing wave 2215
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8/20/2019 Heat transfer from a cylinder in an acoustic standing wave
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n=0 yr2(n «)2 1+ yr2(n «)2(X2/L2)
Xexp gs '•+ L2 t . (A4)
The amplitudesof the successiveerms fall off initially
like (n+ 1/2)-2;comparedo n=0, n= 1 is alreadyeduced
bya factor f 9. Once2(n + 1/2)2>L/X, hey alloffeven
fasten (In the experiments, X.Thereforeany temporalvariationof T• appears nly as
a correction to the correction.
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2216 J. Acoust.Soc. Am., Vol. 98, No. 4, October1995 George Mozurkewich: eat transfer n an acoustic tandingwave 2216