Delft University of Technology
A static and free vibration analysis method for prismatic composite beams with a
non-uniform flexible shear connection
Nijgh, Martin; Veljkovic, Milan
DOI
10.1016/j.ijmecsci.2019.06.018
Publication date
2019
Document Version
Final published version
Published in
International Journal of Mechanical Sciences
Citation (APA)
Nijgh, M., & Veljkovic, M. (2019). A static and free vibration analysis method for non-prismatic composite
beams with a non-uniform flexible shear connection. International Journal of Mechanical Sciences, 159,
398-405. https://doi.org/10.1016/j.ijmecsci.2019.06.018
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International Journal of Mechanical Sciences 159 (2019) 398–405
ContentslistsavailableatScienceDirect
International
Journal
of
Mechanical
Sciences
journalhomepage:www.elsevier.com/locate/ijmecsci
A
static
and
free
vibration
analysis
method
for
non-prismatic
composite
beams
with
a
non-uniform
flexible
shear
connection
Martin
Paul
Nijgh
∗,
Milan
Veljkovic
Faculty of Civil Engineering and Geosciences , Delft University of Technology, Stevinweg 1, 2628 CN, Delft, The Netherlands
a
r
t
i
c
l
e
i
n
f
o
Keywords: Composite beam Analytical modelling Eigenfrequency Tapered beam Sustainabilitya
b
s
t
r
a
c
t
Steel-concretecompositebeamsarewidelyusedinpracticebecauseoftheireconomiccross-sectiondesign.As sustainabilitybecomesmoreandmoreimportantintheconstructionindustry,thedesignofcompositebeamsmust beadaptedtomeettherequirementsofthecirculareconomy.Thiscallsfordemountabilityandreusabilityofthe structuralcomponents,aswellasoptimizeduseofmaterials,forexamplebyusingnon-prismaticbeams. Linear-elasticdesignandthe(optimized)useofdemountableshearconnectorsarekeyinthedesignofreusablecomposite structures.Inthispaper,analyticalpredictionmodelsfortheelasticbehaviourandthefirsteigenfrequencyof non-prismaticcompositebeamswithnon-uniformshearconnectorarrangementsarederived.Theapproachis basedon6thand2ndorderdifferentialequationsusedtodefinematrixequationsforafinitenumberoflinearized
compositebeamsegments.Theanalyticalmodelsarevalidatedusingexperimentalandnumericalresultsobtained withasimplysupportedtaperedcompositebeam.Theanalyticalmodelsaresuitableforcomprehensivestructural analysisofnon-prismaticcompositebeamswithnon-uniformshearconnection.
1. Introduction
Compositeactionbetweenasteelbeamandaconcretedeckis tradi-tionallyachievedusingweldedheadedstuds.Themechanicalbehaviour of welded headed studsis well established in literature (e.g. [1–4]) andthereforeincludedindesigncodes.Althoughtheuseofthewelded headedstudiswidespread,themaindrawbackofthistypeofshear con-nectoristhatitdoesnotallowfornon-destructiveseparationofthesteel beamandconcretedeck[5,6].Oncethebuildinghasbecomeobsolete, demolitionistheonlyoptiontotakethebuildingapart.
Demountableshearconnectorsareincreasinglygaininginterestin theresearch fieldof compositestructures, astheydoallow for non-destructiveseparationofthesteelbeamandconcretedeckandthereby scorecomparativelybetterinsustainabilityassessment. Demountabil-ityoftheshearconnectionoffersthepossibilitytoreusethestructure, eitherbychangingthefloorplantoallowfordifferentfunctionaluse and/orbyre-erectingtheentirestructure atanotherlocation.By de-signingastructuretobesuitablefordemountabilityorreusability,its servicelifetimeisnolongercontrolledbyitsfunctionallifetimeona specificconstructionsitebutbyitstechnicallifetime[7].
Themainbarrierstodesigningdemountableandreusablecomposite structureshavebeenidentifiedbyTingly&Davison[8]as:
• Perceivedriskinspecifyingreusedmaterials,
• Additionalcostsrelatedtothemeasuresrelatedtodemountability,
∗Correspondingauthor.
E-mailaddress:M.P.Nijgh@tudelft.nl (M.P.Nijgh).
• Compositeconstruction,
• Lackofareusedmaterialmarket,
• Longerdeconstructiontime.
Thepotentialbarriersmustbemitigatedtoallowthe implementa-tionofdemountableandreusablestructuresin practice.The feasibil-ity ofconstructionandexecutionof demountableandreusable com-posite beamswasrecentlydemonstratedbyNijghetal.[9]byusing largeprefabricatedconcretedecks,ataperedsteelbeamand demount-ableshearconnectors,incombinationwithoversizedholesand resin-injectedbolts.Inaddition,investigationsareon-goingwhich address the(de)constructiontimeandadditionalcostsrelatedtodemountable andreusablecompositestructures.
Steel-concrete compositebeamsaregenerally prismatic,i.e.their cross-sectiondoesnotvaryalongthebeamlength.However,tapered compositebeamsofferbothstructuralandfunctionaladvantages com-paredwithprismaticcompositebeams.Recently,Nijghetal.[9] con-ductedexperimentstodeterminetheelasticmechanicalbehaviourof taperedcompositebeamswithvariousarrangementsofdemountable shearconnectors.Itwasfoundthattheelasticbehaviourofsimply sup-portedcompositebeamscouldbeoptimisedbyconcentratingtheshear connectorsnearthesupports.Thisfindingisinlinewiththetheoretical predictionsbyRoberts[10]andLinetal.[11].
Thedesignof compositebeamsis governedeitherby serviceabil-itycriteriaorbyitsresistanceintheultimatelimitstate.Inboth de-signcases,acompositebeamcanbedesignedtobedemountableand
https://doi.org/10.1016/j.ijmecsci.2019.06.018
Received31January2019;Receivedinrevisedform29May2019;Accepted8June2019 Availableonline9June2019
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405
reusableaslongastheelasticlimitsarenotexceeded.Inaddition,the perceptionofhumancomfortmustbeconsideredbydesigningfora suf-ficientlyhighfirsteigenfrequency.
InthecomparativestudyofRanzietal.[12],fourdifferentmodelling methodsforcompositebeamsareoutlined:
1 Exactanalyticalmethods 2 Finitedifferencemethod 3 Finiteelementmethod 4 Directstiffnessmethod
Exactanalyticalmethodsarebasedonsolvingdifferentialequations obtained byconsideringthe straindiagramandinternal equilibrium of compositebeams. Theelasticmechanical behaviour of composite beamswith flexible(non-rigid) shear connectors was firstdescribed analyticallybyNewmarketal.[13].TheNewmarkmodelconsistsof twoEuler-Bernoullibeams(onerepresentingthesteelbeam,andthe otherrepresentingtheconcretedeck)whicharecoupledatthe inter-faceusingauniformlydistributedshearconnection.Girhammar&Pan
[14]andGirhammar[15]studiedtheelasticbehaviourofcomposite beamsusingtheNewmarkapproach,whereasXu&Wu[16]andSchabl etal.[17]alsoimplementedsheardeformationintheirmodelsbyusing Timoshenkobeamtheory.Yam&Chapman[18]extendedtheoriginal Newmarkmodeltoaccountfornonlinearmaterialandshear connec-torbehaviour.Theexactanalyticalmethodsarenotdirectlysuitable foraccountingfornon-uniformshearconnectorarrangements.An at-tempttomodelnon-uniformshearconnectorarrangementsusing ana-lyticalmethodswasmadebyLawsonetal.[19]byassumingtheslip distributiontobecosinusoidal.However,theshapefunctionoftheslip distributionalongthebeamlengthmightnotbereadilypredefinedfor non-prismaticcompositebeamswith(highly)non-uniformshear con-nectorarrangements.
Finitedifferencemethodsapproximatethebehaviourofcomposite beamsnumericallybyassumingderivativesintheformofalgebraic ex-pressions.Thismodellingmethodhasbeendeveloped extensivelyby Adekola[20],Roberts[10],andRoberts&Al-Amery[21].
Finiteelementmethodsprovidenumericalsolutionsandarerobust andreliableincasesuitableshapefunctionsarechosen[12]to approx-imatethedisplacements.Thefiniteelementformulationsarebasedon Euler–Bernoullibeamtheory(e.g.[22,23]),Timoshenkobeamtheory (e.g.[24,25])orhigherorderbeamtheories(e.g.[26,27]).
Thedirectstiffnessmethodisbasedonaninitiallyundeformed el-ementthatissubjectedtoaunitrotationortranslationinoneofthe degreesoffreedom(DOF),whilstrestrainingallotherDOFs.Thedirect stiffnessmethodispresentedintheworkofRanzietal.[28],andlater extendedbyRanzi&Bradford[29]toaccountfortime-dependent ef-fects.
Inthiswork,analyticalpredictionmodelsfortheelasticbehaviour andthefirst eigenfrequencyof non-prismatic compositebeamswith non-uniform shear connector arrangement are derived. The starting pointforthepredictionmodelsistodiscretisethecompositebeaminto segments,whichindividuallyfulfilthebasicassumptionsofthe analyt-icalNewmarkmodel.Theresultsoftheproposedanalyticalmodelsfor non-prismaticcompositebeamswithnon-uniformshearconnector
ar-rangementsarecomparedwiththeresultsofactualexperimentsand/or theresultsoffiniteelementanalysis.
2. Theoreticalbackground
Thestartingpointfortheanalyticalmodelsfortheelasticmechanical behaviourandeigenfrequencyofnon-prismaticcompositebeamsisthe partialdifferentialequation,Eq.(1)[16],validforprismaticcomposite beamswithuniformlydistributedflexibleshearconnectorssubjectto bendingdeformation.ForthederivationofEq.(1),thereaderisreferred totheworkofXu&Wu[16].Otherresearchers(e.g.Girhammeretal.
[30])havealsoderivedEq.(1),althoughwithdifferentnotations.
𝜕6𝑤 𝜕𝑥6 −𝛼 2𝜕4𝑤 𝜕𝑥4 +𝛽 2𝛾 1 𝜕 4𝑤 𝜕𝑥2𝜕𝑡2−𝛼 2𝛾 1𝜕 2𝑤 𝜕t2 =− 𝛼2 𝐸𝐼∞ 𝑞+ 1 𝐸𝐼0 𝜕2𝑞 𝜕𝑥2. (1) 𝛼2= 𝐾⋅ 𝑟 𝐸𝐼0 ( 1− 𝐸𝐼0 𝐸𝐼∞ ) ; 𝛽2= 𝐸𝐼∞ 𝐸𝐼0 ;𝛾1= 𝑚 𝐸𝐼∞ . (2) 𝐾=𝑘sc 𝑠 ; 𝑚=𝜌s𝐴s+𝜌deck𝐴deck (3)
InEq.(1),wisthedeflectionfunctionand𝛼2,𝛽2and𝛾
1are
geometri-calandshearconnectionparametersdefinedinEq.(2).Thedistributed load(forceperunitlength)actingonthebeamisdenotedbyq.EI∞
and𝐸𝐼0denotethebendingstiffnessincaseofrigidandnoshear
con-nection,respectively.Thedistancebetweentheelasticneutralaxesof theconnectedmembersundertheassumptionofnoshearinteraction isrepresentedbyr.Thesmearedshearconnectionstiffnessisdenoted byK,andisdefinedastheshearconnectorstiffnesskscdividedbythe
(uniform)connectorspacings.Themassperunitlengthisdenotedby
m.TheconventionofinternalandexternalactionsisdefinedinFig.1. Thesheardeformationoriginatingfromthetransversalloadisnot includedintheanalysis,becausedeflectionduetobendingisdominant forcompositebeamswithtypicalspanoverdepthratios.Therotational inertiaisalsodisregardedbecauseitsinfluenceonthelower eigenfre-quenciesisnegligible[16].
Eq.(1)isonlyvalidforprismaticbeamswithuniformlydistributed shearconnectors.AdiscretisationofthebeamintoJsegmentsis per-formedalongthelengthofthecompositebeamtoaccountonthe non-uniform shear connector arrangements andvarying geometryof the compositebeam.SuchadiscretisationprocesswasfirstadoptedbyTaleb &Suppiger[31]tomodelthefreevibrationsofnon-compositebeams, butsuchanapproachhasnotyetbeenappliedtocompositebeamswith aflexibleshearconnection.Thediscretisationprocesscreatesastepped beamwithdifferentgeometricalandmechanicalpropertiesineach seg-ment,asillustratedinFig.2.Thegeometricalandmechanicalproperties ofasegmentaredeterminedbasedonthemagnitudesoftheinfluencing variablesinthesegment’scentre.Ineachsegment,theshearconnection isassumedcontinuous(smeared)overthesegmentlength.Itisassumed thatallmaterialsbehaveelasticallyandthatthecurvatureofthe con-stituentmembersisequalineachcross-section.Therefore,eachbeam segmentfulfilsthebasicassumptionsoftheNewmarkmodel.
Fig.1.Conventionofinternalactionsinthedifferentialelementofacompositebeamwithaflexibleshearconnection.Theresultantofthenormalforceiszero undertheassumptionthatnoexternalaxialloadisapplied.
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405
Fig.2. Discretizationofataperedcompositebeam(dashedline)intoJprismatic compositebeamsegmentsofequallength,subjecttoauniformlydistributed load.
2.1. Staticanalysis
Forcompositebeamssubjecttostaticuniformlydistributedloads,
Eq.(1)reducesto 𝑑6𝑤 𝑑𝑥6 −𝛼 2𝑑4𝑤 𝑑𝑥4 =− 𝛼2 𝐸𝐼∞𝑞 + 1 𝐸𝐼0 𝑑2𝑞 𝑑𝑥2. (4)
DiscretisingthebeamintoJsegmentsofequallength(seeFig.2), andassumingthattheappliedloadperunitlengthqisconstantineach beamsegment,Eq.(4)furtherreducesto
𝑑6𝑤 𝑗 𝑑𝑥6 −𝛼 2 𝑗 𝑑4𝑤 𝑗 𝑑𝑥4 =− 𝛼2 𝑗 𝐸𝐼∞,𝑗 𝑞𝑗, (5)
with1≤j≤J.Thesolutiontothissixthorderlineardifferentialequation isgivenby 𝑤𝑗(𝑥)=𝐶1,𝑗 e𝛼𝑗𝑥 𝛼4 𝑗 +𝐶2,𝑖 e−𝛼𝑗𝑥 𝛼4 𝑗 +𝐶3,𝑗𝑥3+𝐶4,𝑗𝑥2+𝐶5,𝑗𝑥+𝐶6,𝑗+ 1 24 𝑞𝑗𝑥4 𝐸𝐼∞,𝑗. (6) ExpressionsforthebendingmomentM,shearforceV,shearflowVs,
normalforceN1andinterlayerslipΔuaregivenbyEqs.(7)–(11), re-spectively[14,16,30]. 𝑀𝑗=𝐸𝐼∞,𝑗 𝛼2 𝑗 [ −𝑑 4𝑤 𝑗 𝑑𝑥4 +𝛼 2 𝑗 𝑑2𝑤 𝑗 𝑑𝑥2 + 𝑞𝑗 𝐸𝐼0,𝑗 ] (7) 𝑉𝑗=−𝑑𝑑𝑥𝑀𝑗 = 𝐸𝐼𝛼∞2,𝑗 𝑗 [ 𝑑5𝑤 𝑗 𝑑𝑥5 −𝛼 2 𝑗 𝑑3𝑤 𝑗 𝑑𝑥3 − 1 𝐸𝐼0,𝑗 𝑑𝑞𝑗 𝑑𝑥 ] (8) 𝑉s,𝑗=𝑟1 𝑗 [ 𝑉𝑗+𝐸𝐼0,𝑗 𝑑3𝑤 𝑗 𝑑𝑥3 ] (9) 𝑁1,𝑗= 𝐸𝐼∞,𝑗 𝛼2 𝑗𝑟𝑗 [ −𝑑 4𝑤 𝑗 𝑑𝑥4 +𝛼 2 𝑗 ( 1− 𝐸𝐼0,𝑗 𝐸𝐼∞,𝑗 )𝑑2𝑤 𝑗 𝑑𝑥2 + 𝑞𝑗 𝐸𝐼0,𝑗 ] (10) Δ𝑢𝑗= 𝑑𝑁1,𝑗 𝑑𝑥 1 𝐾𝑗 (11)
The6Jintegrationconstants(C1,1,C2,1...C5,J,C6,J),resultingfrom
the J segments in which Eq. (6) is defined, can be solved by im-posing boundary conditions at x0 and xJ, and interface conditions at x1...xJ−1. For a beamsimply supported at x0=0 andxJ=L, the
sixboundaryconditionsarew1(0)=0,wJ(L)=0,M1(0)=0,MJ(L)=0,
w′′′′1 (0)=q1/EI0,1andw′′′′J (L)=qJ/EI0,J.Forasymmetricalsimply
supportedcompositebeam, theboundaryconditionscan alsobe ex-pressedatxJ=L/2as𝑤′𝐽(𝐿∕2)=0,VJ(L/2)=0,andΔuJ(L/2)=0.Other
typesofsupportingconditionscanbeincludedbymodifyingthe bound-ary conditions appropriately. The equilibrium of shear force, bend-ingmomentandnormalforce,aswellasthecontinuityofdeflection, slopeandslipisenforcedattheinterface ofneighbouringsegments. Theseinterfaceconditionsareexpressedaswj(xj)=wj+1(xj),𝑤′𝑗(𝑥𝑗)=
𝑤′
𝑗+1(𝑥𝑗), Mj(xj)=Mj+1(xj), Δuj(xj)=Δuj+1(xj), Vj(xj)=Vj+1(xj), and
N1,j(xj)=N1,j+1(xj).Anyconcentratedforcescanbeappliedbyimposing
theseintheinterfaceconditionsrelatedtotheverticalforceequilibrium.
2.2. Freevibrationanalysis
Then-theigenfrequencyofaprismaticbeamwithaspanL,a uni-formlydistributedmassmandconstantbendingstiffnessEIisgivenby
𝑓𝑛=𝐾2𝜋𝑛
√
𝐸𝐼
𝑚𝐿4, (12)
inwhichKnisaconstantdependingontheboundaryconditions.The
mostimportantobservationfromEq.(12)isthat𝑓𝑛∼
√
𝐸𝐼.Assuming thatthebendingstiffnessofthebeamAwiththen-theigenfrequency
fn,AisEIA,andthatthemassperunitlengthandthespanofthebeam
AandBareequal,then-theigenfrequencyofthebeamBequals
𝑓𝑛,B=𝑓𝑛,A
√
𝐸𝐼B
𝐸𝐼A.
(13)
Fortaperedcompositebeams,thebendingstiffnessisnotconstant along thebeamaxis,andtherefore thedeflectionat mid-spanunder theself-weightcanbeassumedtobeameasureforthebeamstiffness instead.Theprecedingleadstothehypothesisthatthenaturalfrequency ofataperedcompositebeamcanbedeterminedusingtheexpression
𝑓𝑛=𝑓𝑛,∞
√
𝑤m,∞
𝑤m
, (14)
inwhichfn,∞isthen-thnaturalfrequencyofthe(non-prismatic)
com-posite beamundertheassumptionofrigidshearconnection.wmand
wm,∞denotethedeflectionatmidspanbecauseoftheself-weight
im-postedalongthebeamaxisincaseofflexibleandrigidshearconnection, respectively.Themagnitudesofwmandwm,∞foragivenbeamdesign
canbecomputedusingtheanalyticalmethodpresentedinSection2.1. Thenaturalfrequencyfn,∞ofthecompositebeamwithrigidshear
connectioncanbedeterminedusingEq.(15)[31],whichisbasedon Euler-Bernoullibeamtheory.
𝐸𝐼∞𝜕 4𝑤(𝑥,𝑡)
𝜕𝑥4 =𝑚
𝜕2𝑤(𝑥,𝑡)
𝜕𝑡2 (15)
Eq.(15) canbe simplifiedbyusing theprincipleof separationof variablesintheform𝑤(𝑥,𝑡)=𝑤̃(𝑥)exp(𝑖𝜔𝑛𝑡).Insertingthisexpression intoEq.(15)gives
𝑑4𝑤̃ 𝑑𝑥4 −𝜁 4𝑤̃=0, (16) inwhich 𝜁4= 𝑚𝜔 2 𝑛,∞ 𝐸𝐼∞ . (17) InEq.(17),𝜔𝑛,∞isatrialsolutionfortheangulareigenfrequencyof
thefull-interactioncompositebeam.Theangulareigenfrequency𝜔𝑛,∞ andtheeigenfrequencyfn,∞arerelatedtoeachotherby
𝑓𝑛,∞=
𝜔𝑛,∞
2𝜋 . (18)
ThegeneralsolutionofEq.(16)canbeexpressedintheform
̃
𝑤(𝑥)=𝐶1sin(𝜁𝑥)+𝐶2cos(𝜁𝑥)+𝐶3sinh(𝜁𝑥)+𝐶4cosh(𝜁𝑥). (19)
Thegeneralsolutionineachofthebeamsegmentsiswrittenas
̃
𝑤𝑗(𝑥)=𝐶1,𝑗sin(𝜁𝑗𝑥)+𝐶2,𝑗cos(𝜁𝑗𝑥)+𝐶3,𝑗sinh(𝜁𝑗𝑥)+𝐶4,𝑗cosh(𝜁𝑗𝑥), (20)
with 𝜁𝑗4= 𝑚𝑗𝜔2𝑛,∞ 𝐸𝐼∞,𝑗 . (21) 400
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405
Fig.3. (a)OverviewofthecompositebeampresentedintheworkofNijghetal.
[9] .(b)Cross-sectionaldimensionsofthetaperedsteelbeam.
Thecorrespondinginternalactionsaregivenby
𝑀𝑗=𝐸𝐼∞,𝑗
𝑑2𝑤̃ 𝑗
𝑑𝑥2 , (22)
𝑉𝑗=𝑑𝑑𝑥𝑀𝑗. (23)
The4•Jintegrationconstants,resulting fromtheJsegmentsin whichEq.(20)isdefined,canbesolvedbyimposingboundary condi-tionsatx0andxJ,andinterfaceconditionsatx1...xJ−1.Forasimply
supportedbeamsupportedatx0=0andxJ=L,theboundaryconditions
atthesupportsarew1(0)=0,wJ(L)=0,M1(0)=0andMJ(L)=0.The in-terfaceconditionsareexpressedas𝑤̃𝑗(𝑥𝑗)=𝑤̃𝑗+1(𝑥𝑗),𝑤̃′𝑗(𝑥𝑗)=𝑤̃′𝑗+1(𝑥𝑗),
Mj(xj)=Mj+1(xj),andVj(xj)=Vj+1(xj).Itshouldbenotedthatthefull
beammustbemodelledtofindalleigenfrequenciesand–modes:if
sym-metryconditionsareused,onlytheodd-numberedeigenfrequenciesand -modes(n=1,3,5,…)canbefound.
Byinsertingtheboundaryconditionsintothegeneralsolutions,a systemofJhomogeneousequationsisobtained.Thesystemof homoge-nousequationscanbewrittenas
[A]{c}={0}, (24)
in which {c}=[C1,1C2,1...C5,JC6,J] and [A] is thecoefficient matrix.
Non-trivialsolutionsofEq.(24)canonlybefoundifthedeterminantof thecoefficientmatrixiszero,henceif
det[A]=0. (25)
Incasedet[A]=0,theangulareigenfrequency𝜔𝑛wasassumed cor-rectly in Eq.(21). Incase det[A]≠ 0, anothertrialsolution mustbe adoptedtofindtheangulareigenfrequency.Wuetal.[32]proposed tofindtheangulareigenfrequencybysteppingthroughasequenceof smallincrementsof𝜔𝑛andcomputingthesignforthedeterminantof [A].Ifthesignofthedeterminantof[A]changes,anapproximationfor theangulareigenfrequencyisobtained,which canbefurtherrefined usingthebisectionmethod.
Afterdetermining𝜔𝑛suchthatdet[A]=0,theeigenfrequencyofthe compositebeamwithrigidshearconnectioncanbedeterminedbased onEq.(18).Theeigenfrequencyforacompositebeamwithaflexible shearconnectioncanthenbedeterminedusingtheproposedexpression inEq.(14).Theparameterswmandwm,∞inEq.(14)canbedetermined
usingtheanalyticalmethodpresentedinSection2.1.
Fig.4. Cross-section(side-view)ofcompositebeamstudiedbyNijghetal.[9] .Twoprefabricatedsolidconcretedecksaresupportedbytwotaperedsteelbeams withaspanof14.4m.Loadsareappliedat4.05mfromthesupports.Thec.t.c.distancebetweenthesteelbeamsis2.6m.
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405 Fig.5.Shearconnectorarrangements consid-ered in the work of Nijgh et al. [9] . Each colouredboxindicatesapairoffasteners(one persteelbeam).Resin-injectedboltsprovide shearconnection;normalboltsareplacedonly topreventverticalseparationofthedeckand beam. “U” denotesuniform connector spac-ing,“C” denotesconcentratedconnector spac-ingnearthesupports.Thebeamissymmetric intheplaneatx=L/2.(Forinterpretationof thereferencestocolourinthisfigurelegend, thereaderisreferredtothewebversionofthis article.)
3. Comparisonwithexperimental/numericalresultsand discussion
3.1. Staticanalysis
TheanalyticalmethodpresentedinSection2.1isvalidatedagainst actualbeamtests performedbyNijghetal.[9]on tapered prefabri-catedcompositebeamswithvariousshearconnectorarrangements.The simply-supportedcompositebeam(seeFig.3a)consistsoftwo prefabri-catedsolidconcretedecksof7.2mby2.6m,connectedtotwo symmetri-callytaperedsteelbeamsusingdemountableshearconnectors.The com-positebeamspans14.4mandissubjectedtobendingbyapplyingpoint loadsat4.05mfromthesupports.Aschematicdrawingofthe speci-menisshowninFig.4.Theheightofthesymmetricallytaperedsteel beamsvarieslinearly betweenthesupports,hs(x=0;x=L)=590mm,
andmidspan,hs(x=L/2)=725mm.Thecross-sectionaldimensionsof thetaperedsteelbeamarepresentedinFig.3b.Theconcretedeckhasa constantthicknessof120mmalongitslengthanditisassumedthat
Edeck=33GPa[33]. Theshear connector stiffness ksc was previously determinedas55kN/mm[9].Theshearconnectorarrangements pre-sentedinFig.5wereconsideredintheexperimentalprogramme.
Asensitivitystudyiscarriedouttodeterminetheminimumnumber ofbeamsegmentsperhalf-span(J)thatarenecessarytobemodelled, suchthatthedeflectionatmidspanbasedonJsegmentsconvergesto thevalueobtainedforJ→ ∞.Thisanalysisisperformedunderthe as-sumptionofauniformlydistributedloadandauniformlydistributed shearconnectionwithK=367kN/mm2(equivalenttoshearconnector
arrangementU-24)forthecompositebeampreviouslyintroduced.The resultsofthissensitivitystudyarepresentedinFig.6,indicatingthata smallnumberofsegmentsissufficientforconvergenceofthedeflection atmidspan.ForJ≥3theerrorregardingmidspandeflectioncompared withJ→ ∞ issmallerthan1%.Astheexperimentalbeam[9]offersthe possibilitytoinstall24pairsofshearconnectorsineachhalf-span,the theoreticalbeamisconvenientlysubdividedintoJ=24segmentsper half-span.
Theresultsobtainedusingtheproposedanalyticalmethodarelisted inTable 1, togetherwiththeexperimentalandfinite-elementresults obtainedbyNijghetal.[9].Theresultsareexpressedintermsofthe effectivebendingstiffnessandtheeffectiveshearstiffnessofthe
com-positebeam,respectivelydefinedas
𝑘b,ef f=
Δ𝐹
Δ𝑤(𝑥=𝐿∕2);𝑘s,ef f= Δ𝐹
Δ𝑢(𝑥=0). (26) InEq.(26),ΔFistheforceincrement,ΔW(x=L/2)isthedeflection incrementatmidspanandΔu(x=0)istheslipincrementatthesupports. Theseparameterswereevaluatedatlinear-elasticloadlevels.
Fig.7,Fig.8andTable1clearlyshowthattheproposedanalytical modelandthefiniteelementresults[9]areingoodagreement regard-ingtheeffectivebendingstiffnessandtheeffectiveshearstiffnessforall theconsideredshearconnectorarrangements.Thenumericaland ana-lyticalpredictionscloselymatchtheexperimentalresultsregardingthe effectivebendingstiffness,withaveragedeviationsof only0.4%and 2.4%,respectively.Largedeviationexistsregardingtheeffectiveshear stiffness,aswasalreadyobservedin[9].Onaverage,theactualend-slip is47%smallerthanpredictedusingtheproposedanalyticalmodel.The sourceofthisdeviationisnotconsideredinthispaper.Theproposed analyticalmodel,however,showsgoodagreementwiththefinite ele-mentmodel[9]withanaveragedeviationofonly6%.Thisindicates thatthelargedeviationbetweenanalyticalmodelandexperimental re-sultsislikelyrelatedtotheexperimentsandnottothepresentanalytical modelnortothefiniteelementanalysis[9].
Fig.6. Relativedeflectionofthetaperedcompositebeamsubjecttoauniformly distributedload,asafunctionofthenumberofsegmentsJperhalf-span. 402
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405 Table1
Resultsobtainedusingproposedanalyticalmodel(presentstudy)andtheexperimentallyandnumerically obtainedresultsbyNijghetal.[9] regardingeffectivebendingstiffnessandeffectiveshearstiffnessfor theconsideredshearconnectorarrangements.
kb,eff(kN/mm) ks,eff(kN/mm)
Arrangement Analytical model Experiment FE model Analytical model Experiment FE model
U-24 7.25 6.89 7.13 285 514 301 C-12 7.04 6.69 6.96 269 487 294 C-6 6.31 6.18 6.28 190 389 188 U-12 6.60 6.35 6.53 177 330 190 U-6 5.90 5.82 5.87 120 199 128 U-0 3.96 4.10 4.07 46 98 51
Fig.7. Theeffectivebendingstiffnessparameterobtainedusingtheproposed analyticalmethod,comparedwiththeexperimentallyandnumericallyobtained results[9] ,forthedifferentshearconnectorarrangements.
Fig.8. Theeffectiveshearstiffnessparameterobtainedusingtheproposed an-alyticalmethod,comparedwiththeexperimentallyandnumericallyobtained results[9] ,forthedifferentshearconnectorarrangements.
Presentstudyconfirmsthatthedeflectionandshearconnectorslip canbeminimizedbyconcentratingtheshearconnectorsnearthe sup-portsofasimplysupportedbeam.Byoptimizingtheshearconnector ar-rangementthetotalnumberofshearconnectorscanbereduced,which hasapositiveimpactonthespeedof(de)constructionandthematerial andlabourcosts.Bothparametersarekeytothesuccessful implemen-tationofdemountableandreusablestructureswithintheconstruction industry[8].
Theslipdistributionalongthetaperedcompositebeamsubjectedto auniformlydistributedloadq(F=0)isshowninFig.9forthedifferent shearconnectorarrangements.Thisloadcasecorrespondstoapractical beamapplication.Fig.9indicatesthattheassumptionofLawsonetal.
[19]ofacosinusoidalshapefunctionfortheinterlayerslipisnot gener-icallyvalid:particularlyin thecaseofshearconnectorsconcentrated nearthesupports(arrangementsC6andC12)amorerefinedanalysis usingthepresentmethodmustbecarriedouttodeterminetheactual slipdistributionandthecorrespondinginternalactions.
Fig.9. Shapeofslipdistributionalongthelengthofthetaperedcompositebeam subjectedtoauniformlydistributedloadq(F=0),comparedtothecosinusoidal distributionassumedbyLawsonetal.[19] .
3.2. Freevibrationanalysis
Thefirsteigenfrequencyofthetaperedcompositebeampresentedin
Section3.1isdeterminedfortheshearconnectorarrangementslisted in Fig.5andforvariousmagnitudesof theshear connectorstiffness
ksc (25,55and100kN/mm).Inthisanalysis,thecompositebeamis regardedaspartofalargerstructureandthatthereforeonetapered compositebeameffectivelyconsistsofonetaperedsteelbeamandtwo prefabricatedconcretedecks.
Theresultsofasensitivitystudytodeterminetheminimumnumber ofbeamsegmentsperhalf-spanJtoensureanaccuratelypredictionof thefirsteigenfrequencyarepresentedinFig.6.Theanalysishasbeen conductedwiththesameassumptionsasfor thesensitivitystudy re-gardingthedeflection.AlsointhiscaseitisfoundthatforJ≥3the convergenceerrorintermsoffirsteigenfrequencyissmallerthan1%. AllcalculationsarecarriedoutbysubdividingthebeamintoJ=24 seg-mentsperhalf-spantomatchthesegmentationusedinSection3.1.
Theanalyticalmethodtodeterminetheeigenfrequenciesofa non-prismaticcompositebeamwithflexibleshearconnectorsisvalidatedby
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405 Table2
FirsteigenfrequenciesofthetaperedcompositebeampresentedinSection 3.1 forvariousshear con-nectorarrangementsandshearconnectorstiffness,obtainedusingtheproposedanalyticalmodeland usingfiniteelementanalysis.
Arrangement
fn,∞,FEA fn,∞,analytical ksc 𝑤 m,∞∕ 𝑤 m fn,analytical fn,FEA fn,analytical / f n,FEA
(Hz) (Hz) (kN/mm) (-) (Hz) (Hz) (-) U-24 5.39 5.51 25 0.82 4.99 5.00 0.998 55 0.9 5.23 5.17 1.012 100 0.94 5.34 5.25 1.017 C-12 25 0.79 4.88 4.92 0.992 55 0.87 5.14 5.10 1.007 100 0.92 5.27 5.20 1.013 C-6 25 0.69 4.59 4.71 0.975 55 0.78 4.88 4.89 0.997 100 0.84 5.03 5.00 1.007 U-12 25 0.73 4.71 4.81 0.978 55 0.84 5.04 5.02 1.002 100 0.9 5.22 5.15 1.013 U-6 25 0.64 4.41 4.61 0.957 55 0.75 4.78 4.85 0.987 100 0.83 5.02 5.00 1.004 U-0 0 0.44 3.65 3.67 0.995 Average 0.997
Fig.10. Eigenmodesofthetaperedcompositebeam.
finiteelementanalysis.Thesimplysupportedcompositebeamis mod-elledinABAQUS/Standardusingfour-nodeshellelements(S4)forthe taperedsteelbeamandconcretedeck.Theshearconnectorsare mod-elledusingmesh-independent,point-basedfastenerswithaspring stiff-nessequaltoksc.
Theresultsobtainedusingtheanalyticalandnumericalmodelsare presentedinTable2.Onaverage,thefirsteigenfrequencyobtainedby theproposedanalyticalmodelis0.3%lowerthanpredictedbythe fi-niteelementmodel.Thefirsteigenfrequencyisunderestimatedincase ofaweakshearconnectionandoverestimatedincaseofastrongshear connection,withamaximumdeviationof4.3%fortheU-6casewith
ksc=25kN/mm.Theproposedanalyticalmodelisthereforeconsidered
suitablefordeterminationofthefirsteigenfrequencyofatapered com-positebeamwithnon-uniformshearconnectorarrangements.
Fig.10showsthefirstfivenaturalvibrationmodesofthetapered compositebeam.Good agreementbetween theanalyticalmodeland finiteelementmodelisobservedintermsofmodalshape.Thehigher
Table3
Natural frequencies for the ta-pered composite beam with a rigidshearconnection.
n fn,∞,analytical √ 𝑓1,∞,analytical 𝑓𝑛,∞,analytical (-) (Hz) (-) 1 5.51 1.00 2 21.2 1.96 3 47.9 2.94 4 84.7 3.92 5 132.5 4.90
ordernaturalfrequenciesofthetaperedcompositebeamarelistedin
Table3.Itisobservedthatthehigher-ordernaturalfrequenciesarenot equaltof1n2,asisthecaseforprismaticbeams,butareslightlysmaller
becauseofthenon-uniformmassandbendingstiffnessdistributions.
5. Conclusions
Themainoutcomesofthetheoreticalandnumericalassessmentof thedeflectionandfirsteigenfrequenciesof(reusable)taperedcomposite beamsareasfollows:
• Theproposedanalyticalmethodsprovideaneasytouseformulation toassessthestructuralresponseofacompositebeamintheelastic stage.
• Theproposedanalyticalmethodrequiresdiscretisationintoa lim-itednumberofsegmentsalongthebeamlengthtoobtainaccurate results.Discretisingthebeaminto3segmentsperhalf-spanleadsto convergenceofthedeflectionandthefirsteigenfrequencyforthe compositebeamstudiedinthiswork.
• Theproposedanalyticalmethodaccuratelypredictsthedeflectionof taperedcompositebeams.Onaverage,thedeviationoftheproposed analyticalmethodregardingmidspandeflectionis2.4%compared withtheexperimental resultsand0.4%compared withthefinite elementresultsofNijghetal.[9].
• Predictionsregardingendslipobtainedusingtheproposed analyti-calmethodareinlinewithfiniteelementanalysis,withanaverage deviationof6%.Theanalyticalandnumericalmodeldonot repro-ducetheendslipobtainedintheexperimentalworkofNijghetal.
[9].Discussionofreasonsforsuchscatteringisleftoutofthescope ofthiswork.
M.P. Nijgh and M. Veljkovic International Journal of Mechanical Sciences 159 (2019) 398–405
• Theshapeoftheslipdistributionalongthelengthofanon-prismatic compositebeamisnotnecessarilycosinusoidal,particularlyfor non-uniformshearconnector arrangements.Thislimitsthevalidityof theLawsonmodel[19].Therefore,itisrecommendedtousepresent methodtodeterminetheactualslipdistributionandthe correspond-inginternalactions.
• Verygood agreementis found between theeigenfrequencies ob-tained using finite element analysis and the proposed analytical model.Onaverage,theproposedanalyticalmodelunderestimates thefirsteigenfrequencyby0.3%.
Acknowledgment
ThisresearchwascarriedoutunderprojectnumberT16045inthe frameworkoftheResearchProgramoftheMaterialsinnovationinstitute M2i(www.m2i.nl)supportedbytheDutchgovernment.
References
[1] Shaikh AF , Yi W . In-place strength of welded headed studs. PCI J 1985;30(2):56–81 .
[2] Mirza O , Uy B . Effects of the combination of axial and shear loading on the behaviour of headed stud steel anchors. Eng Struct 2010;32(1):93–105 .
[3] Lam D , El-Lobody E . Behavior of headed stud shear connectors in composite beam. J Struct Eng 2005;131(1):96–107 .
[4] Hanswille G , Porsch M , Ustundag C . Resistance of headed studs subjected to fatigue loading: Part I: experimental study. J Construct Steel Res 2007;63(4):475–84 .
[5] Pavlovic M . Resistance of bolted shear connectors in prefabricated steel-concrete composite decks. Belgrade: University of Belgrade; 2013 .
[6] Moynihan MC , Allwood JM . Viability and performance of demountable composite connectors. J Construct Steel Res 2014;99:47–56 .
[7] van den Dobbelsteen A . The sustainable office - an exploration of the potential for factor 20 environmental improvement of office accommodation. Delft: Delft Univer- sity of Technology; 2004 .
[8] Tingly DD , Davinson B . Design for deconstruction and material reuse. In: Proceed- ings of the institution of civil engineers, 164; 2011. p. 195–204 .
[9] Nijgh MP , Girbacea IA , Veljkovic M . Elastic behaviour of a reusable tapered com- posite beam. Eng Struct 2019;183 .
[10] Roberts TM . Finite difference analysis of composite beams with partial interaction. Comput Struct 1985;21(3):469–73 .
[11] Lin JP , Wang G , Bao G , Xu R . Stiffness matrix for the analysis and design of par- tial-interaction composite beams. Construct Build Mater 2017;156:761–72 .
[12] Ranzi G , Gara F , Leoni G , Bradford MA . Analysis of composite beams with partial shear interaction using available modelling techniques: a comparative study. Com- put Struct 2006;84:930–41 .
[13] Newmark NM , Siest CP , Viest CP . Test and analysis of composite beams with incom- plete interaction. In: Proceedings of the Society for Experimental Stress Analysis; 1951. p. 75–92 .
[14] Girhammar UA , Pan DH . Exact static analysis of partially composite beams and beam-columns. Int J Mech Sci 2007;49:239–55 .
[15] Girhammar UA . A simplified analysis method for composite beams with interlayer slip. Int J Mech Sci 2009;51:515–30 .
[16] Xu R , Wu Y . Static, dynamic, and buckling analysis of partial interaction composite members using Timoshenko’s beam theory. Int J Mech Sci 2007;49:1139–55 .
[17] Schnabl S , Saje M , Turk G , Planinc I . Analytical solution of two-layer beam taking into account interlayer slip and shear deformation. J Struct Eng 2007;133(6):886–94 .
[18] Yam LCP , Chapman JC . The inelastic behaviour of simply supported composite beams of steel and concrete. In: Proceedings of the institution of civil engineers, 41; 1968. p. 651–83 .
[19] Lawson RM , Lam D , Aggelopoulos ES , Nellinger S . Serviceability performance of composite beams. In: Proceedings of the institution of civil engineers, 170; 2017. p. 98–114 .
[20] Adekola AO . Partial interaction between elastically connected elements of a com- posite beam. Int J Solids Struct 1968;4:1125–35 .
[21] Al-Amery RIM , Roberts TM . Non-linear finite difference analysis of composite beams with partial interaction. Comput Struct 1990;35(1):81–7 .
[22] Hirst MJS , Yeo MF . The analysis of composite beams using standard finite element programs. Comput Struct 1980;11:233–7 .
[23] Salari MR , Spacone E , Shing PB , Frangopol DM . Nonlinear analysis of composite beams with deformable shear connectors. J Struct Eng 1998;124(10):1148–58 .
[24] Zona A , Ranzi G . Finite element models for nonlinear analysis of steel-concrete com- posite beams with partial interaction in combined bending and shear. Finite Elem Anal Des 2011;47:98–118 .
[25] Schnabl S , Saje M , Turk G , Planinc I . Locking-free two-layer Timoshenko beam ele- ment with interlayer slip. Finite Elem Anal Des 2007;43:705–14 .
[26] Chakrabarti A , Sheikh AH , Griffith M , Oehlers DJ . Analysis of composite beams with partial shear interaction using a higher order beam theory. Eng Struct 2012;36:283–91 .
[27] Uddin MA , Sheikh AH , Brown D , Bennet T , Uy B . A higher order model for in- elastic response of composite beams with interfacial slip using a dissipation based arc-length method. Eng Struct 2017;139:120–34 .
[28] Ranzi G , Bradford MA , Uy B . A direct stiffness analysis of a composite beam with partial interaction. Int J Numerical Methods Eng 2004;61:657–72 .
[29] Ranzi G , Bradford MA . Analysis of composite beams with partial interaction using the direct stiffness approach accounting for time effects. Int J Numerical Methods Eng 2009;78:564–86 .
[30] Girhammar UA , Pan DH , Gustafsson A . Exact dynamic analysis of composit beams with partial interaction. Int J Mech Sci 2009;51:565–82 .
[31] Taleb NJ , Suppiger EW . Vibration of stepped beams. J Aerosp Eng 1961;28:295–8 .
[32] Wu YF , Xu R , Chen W . Free vibrations of the partial-interaction composite members with axial force. J Sounds Vibrations 2007;299:1074–93 .
[33] NEN. EN 1992-1-1: Eurocode 2: design of concrete structures - Part 1-1: general rules and rules for buildings. Delft: NEN; 2005 .