EXTENDED STOKES SERIES FOR DEAN FLOW IN WEAKLY CURVED PIPES
A thesis presented for the degree of Doctor of Philosophy of Imperial College by
Florencia Amalia Tettamanti
Department of Mathematics Imperial College 180 Queen’s Gate, London SW7 2BZ
June 24, 2012 2
I certify that this thesis, and the research to which it refers, are the product of my own work, and that any ideas or quotations from the work of other people, published or otherwise, are fully acknowledged in accordance with the standard referencing practices of the discipline.
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Abstract
This thesis considers steady, fully-developed flows through weakly curved pipes using the extended Stokes series method.
The Stokes series for pipes of circular cross-section is expanded in powers of the Dean number, K, to 196 terms by computer. Analysis shows that the convergence is limited by an imaginary conjugate pair of square-root singularities K = iK . ± c Contrary to previous analysis of this solution, analytic continuation of the series indicates that the flux ratio in a weakly curved pipe does not vary asymptotically as K−1/10 for large K.
Using generalised Pad´eapproximants it is proposed that the singularity at iKc corresponds to a symmetry breaking bifurcation, at which three previously unreported complex branches are identified. The nature of the singularity is supported in part by numerical consideration of the governing equations for complex Dean number.
It is postulated that there exists a complex solution to the governing equations for which the azimuthal velocity varies asymptotically as K−1/2, and the streamfunction as K0 near K =0. This is supported by the results from the generalised Pad´e approximants.
Brief consideration is given to pipes of elliptic cross-section. The Stokes series for pipes of elliptic cross-section for various aspect ratios, λ, is expanded up to the K24 term by computer. For small K, it is found that the flux ratio achieves a minimum for aspect ratio λ 1.75. This, and the behaviour of the total vorticity, is in agreement with previous ≈ studies which found that the effect of the curvature is reduced in the limit of small and large aspect ratios. The convergence of the series solution is found to be limited by an imaginary conjugate pair of square-root singularities K = iK (λ), which varies with λ. ± c 6
Acknowledgements
I would like to thank my supervisor, Jonathan Mestel, for introducing this interesting prob- lem in fluid dynamics to me. His insight, patience and guidance over the last 3 years have been invaluable. I would like to thank Jennifer Siggers for access to her code and guidance in its application. I am grateful also to Slobodan Radosavljevic for sharing his work on this problem with me.
Work aside, thanks to all my friends for providing much needed distractions and support throughout my thesis.
This research was supported by funding from the Mathematics Department of Imperial College London. 7
Table of contents
Abstract 5
1 Introduction 13 1.1 Motivation-thephysicalproblem ...... 13 1.2 Motivation-thetheoreticalproblem ...... 19 1.2.1 DeanEquations...... 20 1.2.1.1 Non-dimensionalisation & boundary conditions . . . .. 22 1.2.2 SolutionstotheDeanequations ...... 24 1.2.2.1 SmallDeannumber ...... 24 1.2.2.2 IntermediateDeannumber ...... 25 1.2.2.3 LargeDeannumber ...... 29 1.2.3 Alternativecross-sections ...... 31 1.3 Aimsofthethesis...... 32 1.4 Organisationofthethesis ...... 33
2 Extended Stokes series: circular cross-section 35 2.1 Computer-extendedseries...... 35 2.2 Radiusofconvergence ...... 40 2.2.1 Domb-Sykesanalysis...... 41 2.2.2 Results ...... 45 2.3 Analyticcontinuation ...... 50 2.3.1 Eulertransform...... 50 2.3.2 Results ...... 52 2.4 Comparisonwithnumerics ...... 61 2.4.1 Flux ratio, total vorticity and outer wall shear stress...... 62 2.4.2 Azimuthalvelocityandstreamfunction ...... 64 2.5 Summaryandconclusions ...... 66
3 Pade´ approximants 67 3.1 GeneralisedPad´eapproximants-procedure ...... 67 3.2 Results...... 70 3.2.1 Real K ...... 71 3.2.1.1 Anillustrativeaccount-thefluxratio ...... 71 3.2.1.2 Discussionof results and comparisonwith other techniques 74 3.2.2 Imaginary K ...... 76 8
3.2.2.1 Anillustrativeaccount-thefluxratio ...... 76 3.2.2.2 Discussionof the complexbifurcation diagram for imag- inary K ...... 81 3.2.2.3 Comparison with numerics of Branch I and II ...... 86 3.2.2.4 Asymptotic analysis of Branch II ...... 86 3.3 Summaryandconclusion ...... 88
4 Numerical solution of the Dean equations for complex K 91 4.1 The complex K finitecurvatureDeanequations ...... 91 4.2 Fictitioustimescheme ...... 93 4.2.1 Overviewoftheprocedure ...... 94 4.2.2 Results ...... 95 4.3 Path-continuation ...... 97 4.3.1 Overviewoftheprocedure ...... 97 4.3.1.1 Simplecontinuation ...... 99 4.3.1.2 Pseudo-arclengthcontinuation ...... 100 4.3.2 Results ...... 102 4.4 Summaryandconclusion ...... 106
5 Extended Stokes series: elliptic cross-section 109 5.1 Governingequations ...... 109 5.2 Asymptotic behaviour for large and small λ ...... 113 5.3 Computer-extendedseries...... 115 5.4 Radiusofconvergence ...... 118 5.5 GeneralisedPad´eapproximants...... 119 5.6 DiscussionoftheextendedStokesseries ...... 120 5.6.1 Contours of azimuthal velocity and streamfunction ...... 120 5.6.2 Cross-sectional velocities for small λ ...... 121 5.6.3 Azimuthal velocity for large λ ...... 123 5.6.4 Totalvorticity...... 124 5.6.5 Fluxratio ...... 127 5.7 Summaryandconclusion ...... 129
6 Final Conclusions 131 6.1 Summaryofkeyresultsandpossibleextensions ...... 131 6.2 Conclusionsandfuturework ...... 133
References 145
A Introduction 146 A.1 Boundarylayerasymptotics ...... 146
B Extended Stokes series: circular cross-section 149 B.1 Expressionfortherecurrencerelation ...... 149 B.1.1 Expanding ωn (r, θ) and ψn (r, θ) ...... 151 B.2 CoefficientsoftheEulertransformedseries ...... 157 9
B.3 Revisiting Van Dyke’s work as K ...... 157 B.3.1 Completingtheseries. . .→∞ ...... 158 B.3.2 Comparison with ln(1 x)α ...... 159 B.3.3 Critical-pointrenormalisation− ...... 159 B.4 ‘Confluent-singularityanalysis’ ...... 160 B.5 Alternativeextrapolationtechniques ...... 162
C Pade´ approximants 166 C.1 LinearPad´eapproximants ...... 166 C.1.1 Results ...... 167 C.2 QuadraticPad´eapproximants...... 170 C.2.1 Results ...... 170 C.3 Generalised Pad´eapproximants: total vorticity Branch II ...... 172 C.4 Generalised Pad´eapproximants: path-continuation ...... 174
D Numerical solution of the Dean equations for complex K 178 D.1 Path-continuation ...... 178
E Extended Stokes series: elliptic cross-section 180 E.1 Derivation of the Dean equations for λ< 1 ...... 180 E.2 Dean equations for λ> 1 ...... 183 E.3 Computer-extendedseries...... 184 E.4 Calculationofthefluxratio...... 188 E.5 Calculationofthetotalvorticity ...... 191 E.6 Cuming’sscaling ...... 192 10
List of Figures
1.1 Pictorial representation of pressure and flow over the cardiaccycle...... 16 1.2 Sketch of streamlines of the azimuthal and secondary velocity in curved pipes...... 17 1.3 Sketch of thestreamlinesof thesecondary velocityin curved pipes as found byLyne[49]...... 18 1.4 Coordinate system for curved pipe with circular cross-section...... 20 1.5 Dean’s series solution: azimuthal velocity and secondary streamlines con- tours...... 25 1.6 Contour plots: two-vortex solution from Siggers & Waters[73]...... 26 1.7 Schematic representation of bifurcation diagram for real K ...... 27 1.8 Contour plots: four-vortex solution from Siggers & Waters[73]...... 28
2.1 Domb-Sykes plot K-series: flux ratio, friction ratio, outer wall shear stress andtotalvorticity ...... 48 2.2 GraphicalrepresentationoftheEulertransform ...... 50 2.3 Domb-Sykes plot ǫ-series: flux ratio, friction ratio, total vorticity and outer wallshearstress...... 54 2.4 Domb-Sykesplotformodelfunctions ...... 57 2.5 Domb-Sykes plot for flux ratio Q(ǫ) ...... 60 2.6 Domb-Sykesplotfor the coefficients of theseries expansion of (1 ǫ)−1/20Q (ǫ) 61 − 2.6 Comparison of the flux ratio, total vorticity and outer wall shear stress ǫ- serieswithnumerics ...... 63 2.7 Comparison of contour plots of ǫ-serieswithnumerics ...... 65
3.1 Schematic representation of bifurcation diagram for imaginary K ..... 70 3.2 Generalised Pad´eapproximant Branch I: example of spurious behaviour for flux ratio for real K ...... 73 3.3 Generalised Pad´eapproximant Branch I: flux ratio for real K ...... 73 3.4 Generalised Pad´eapproximant Branch I: Comparison with numerics and ǫ series...... 76 3.5 Generalised− Pad´eapproximant Branch I and II: example of spurious be- haviour of flux ratio for imaginary K ...... 79 3.6 Generalised Pad´eapproximants Branch I and II: flux ratio for imaginary K 79 3.7 Generalised Pad´eapproximant Branch III : flux ratio for imaginary K ... 81 3.8 Generalised Pad´eapproximant Branch I and II: flux ratio, total vorticity, outer wall shear stress imaginary K ...... 84 LIST OF FIGURES 11
3.9 Generalised Pad´eapproximant Branch III and IV: flux ratio, total vorticity, outer wall shear stress for imaginary K ...... 85 3.10 Generalised Pad´eapproximant Branch I and II: comparison with numerics for imaginary K ...... 86 3.11 Generalised Pad´eapproximant Branch II asymptotics: log-log plot of flux ratio for imaginary K ...... 88
4.1 Flux ratio on Branch I: comparison of fictitious time numerics (TNS) and generalised Pad´eapproximants (GPA) for real and imaginary K ...... 96 4.2 Depictionofsimplecontinuation ...... 99 4.3 Depiction of pseudo-arclength method for path-continuation ...... 101 4.4 Contour plotsof w, ψ and Ω on Branch I for K =0.4i M = 200, κ = 15 . 104 4.5 Contour plots of w, ψ and Ω on Branch II for K = 0.82921i, M = 200, κ = 15 ...... 105
5.1 Coordinate system for curved pipe with elliptical cross-section with small λ 1 ...... 112 5.2 Generalised≤ Pad´eapproximant: elliptic cross-section ...... 119 5.3 Contour plot of azimuthal velocity and streamfunction for λ =0.8 . . . . .120 5.4 Comparing secondary velocity on central axis for varying λ ...... 122 5.5 Comparing azimuthal velocity on center-line for varying λ ...... 123 5.6 Comparing the total vorticity calculated by Cuming [19] and the extended Stokesseries(ESS) ...... 125 5.7 Asymptotic behaviour of the total vorticity for varying λ and small K . . .126 5.8 Comparing the flux ratio calculated by Srivastava [79] and the extended Stokesseries(ESS) ...... 128
B.1 Completingtheseries: fluxandfrictionratio ...... 158
C.1 Linear Pad´eapproximants: estimate of singularities forthefluxratio . . . . 168 C.2 Linear Pad´eapproximants: estimate of asymptotic behaviour ...... 169 C.3 Quadratic Pad´eapproximant: plot of the flux ratio ...... 173 C.4 Generalised Pad´eapproximant Branch I and II: total vorticity for imaginary K ...... 174 C.5 Depictionofturningpointbifurcation ...... 175 C.6 Depictionoftranscriticalbifurcation ...... 175
D.1 Block matrix structure for Jacobian of Dean equations ...... 179
E.1 Coordinate system for curved pipe with elliptical cross-section with large λ 1 ...... 184 E.2 Cuming’s≥ coordinate system for curved pipe with ellipticcross-section . . . 192 12
List of Tables
2.1 Coefficients of K - series: flux ratio, friction ratio, total vorticity and outer wallshearstress ...... 46 −2 2.2 Neville table estimates of Kc : flux ratio, friction ratio, total vorticity and outerwallshearstress ...... 49 2.3 Bottom Row of the Neville Table for (reading left to right), the flux ratio and friction ratio ǫ-series ...... 53 2.4 Neville table estimates of the critical exponent of ǫc:fluxratio ...... 55 2.5 Dominant singularity and corresponding asymptotic behaviour of the ratio of the coefficients of model functions (2.50)- (2.53) ...... 56
3.1 Generalised Pad´eapproximant: estimates of Kc foundusingfluxratio . . . 77
5.1 Values of 0 and λ for which the extended Stokes series has been calculated. 116 5.2 Estimateof Kc for various λ ...... 118 5.3 Valueof x˜max for various λ ...... 121 B.1 Coefficients of ǫ - series: flux ratio, friction ratio, total vorticity and outer wallshearstress ...... 157
C.1 Quadratic Pad´eapproximants: estimate of nearest singularity using the flux ratio,totalvorticityandouterwallshearstress ...... 171 13
Chapter 1
Introduction
The study of flow in curved pipes is a classical problem in fluid dynamics, motivated by its prevalence in many physiological and industrial systems. Herein, the method of computer- extended Stokes series is used to model steady, fully-developed flow through weakly curved pipes. By way of introduction, a brief overview of the physical and theoretical motivations for considering this problem and review of past work are given below. The chapter con- cludes with an overview of the structure of the thesis.
1.1 Motivation - the physical problem
The study of fluid flow in curved and coiled pipes has been driven by the practical impor- tance of many industrial and physiological applications.
In industry, curved and coiled pipes can be found in heat engines, pipe-line transport, chem- ical reactors and other such industrial equipment. Particularly relevant effects of the cur- vature of the pipe on the flow include: (i) migration to the outside bend of the maximal azimuthal velocity (ii) an increase in the pressure drop as compared to that in a straight pipe of the same length [22, 29]; (iii) an increase in the heat-transfer rate [59, 60], which is important in cooling systems; (iv) an increase in the residence time distribution [55], which is important in chemical reactions and (v) a delay in the onset of turbulence compared to a straight-pipe [82]. In particular, in a coiled pipe with a radius of curvature 18 times that of 1.1 Motivation - the physical problem 14 its cross-section, the flow is laminar up to a Reynolds number∗ of 5830, that is almost three times the Reynolds’ criterion for instability in a straight pipe [82]. Whilst, accordingly, curved pipes can be used in industrial applications to improve flow characteristics, they are generally found in practical situations due to spatial constraints. For example, laminar flow through curved pipes occurs in the circulatory system of organisms. Of particular in- terest in physiological fluid dynamics is the modelling of arterial blood flow [67]. Recent studies have focused on understanding the effect of the blood flow in the development of cardiovascular disease, specifically arterial atherosclerosis [73, 74].
Atherosclerosis is a progressive disease, characterised by plaque formation within the arte- rial wall. In addition to narrowing the arterial lumen, plaques may rupture causing thrombo- embolism and distal tissue ischemia. Common examples include miocardial infarction and cerebral vascular accidents, which are the result of coronary and cerebral artery occlusion respectively. Coronary artery atherosclerosis alone is the cause of one third of all deaths in the Western world [92].
Though the mechanism by which atherosclerosis is formed is not fully understood, empir- ical studies have concluded that the plaques predominate in areas of significant curvature and bifurcation within the arterial system, which are associated with flow disturbance. Such areas include the aorta, coronary artery and carotid bifurcation [12, 31, 48]. It is widely accepted that the spatial distribution of atherosclerosis is correlated with areas of low mean wall shear stress and regions where the wall shear stress changes direction, both of which contribute to the stasis of atherogenic material [68]. Consequently, much interest has been given to modelling the aorta, and the cardiovascular system in general, with the aim of providing insight into the sites of plaque development.
There are two main approaches to modelling these flows. The first aims to replicate the system as accurately as possible, using empirical and anatomical data, and studies the fluid flow by full computational fluid dynamic simulations. This procedure has become par- ticularly attractive in recent years due to advances in computational power, refinement of numerical schemes and medical imaging. Reviews of computational modelling in the car- diovascular system are given by Steinman [80], Steinman et al. [81] and more recently
∗Using the well-known Reynolds number aw/ν¯ , where a is the radius of the cross-section, w¯ is the mean velocity flow and ν is the kinematic viscosity. Chapter 1. Introduction 15
Hoskings & Hardmand [41]. The second approach is to idealise the system by, for exam- ple, simplifying the geometry and form of the driving pressure gradient. This leads to a reduced set of equations that can be investigated, if not solved, by mathematical methods (which may of course include computational work). A review of this second approach is given by Pedley [68].
The idealised problem is studied in order to gain insight into the physical one. Accord- ingly, the simplifying assumptions made must have some physical basis. Returning to the discussion of the aortic arch, below its physical attributes and some simplifications of these are explored.
First, the rheology of aortic blood is considered. Strictly speaking, blood is an incompress- ible non-Newtonian fluid - its effective viscosity increases as the stress decreases. This is because blood is a suspension compromising of 40-50% deformable particles, including red blood cells (erythrocytes), white blood cells (leucocytes) and platelets (thrombocytes), and up to 55% of plasma, a colourless Newtonian fluid. In arteries however, where the particle size is appreciably small in comparison to the dimensions of the channel, this deviation is not so marked. Accordingly, arterial blood can be, and is usually, modelled as a Newto- nian fluid. Consequently, its motion can be described by the Navier-Stokes equations. Of course, it is also incompressible.
Furthermore, mathematical models of the arterial system generally neglect entrance effects. As arteries are long compared with their diameter and have a regular cross-section, the assumption of fully-developed flow is perhaps reasonable. In reality however, the flow in the aortic arch is affected by the profile of the flow as it leaves the left ventricle.
The flow in the cardiovascular system is driven by an unsteady pressure gradient, generated by the pumping of the heart. There are two stages to the cardiac cycle shown in Figure 1.1. In the first stage, known as systole, the heart contracts and ejects blood from the heart into the major arteries. During this stage the pressure in the system increases. In the second stage, known as diastole, the heart is relaxed and once more fills with blood. The flow in this final stage is approximately constant. In vivo measurements of the physiological pressure gradients can be used to calculate the flow waverform exactly [80]. However, more simply, the oscillatory behaviour of the cardiac cycle can be captured by a sinusoidal driving pressure gradient. Alternatively, a much simpler model would consider a constant 1.1 Motivation - the physical problem 16 driving pressure gradient. Though this final simplification is perhaps more suitable to areas further away from the heart than the aortic arch.
65 100 pressure 90 pressure (mmHg) flow (m/s) flow 0 flow 70
Systole (0.2 s) Diastole (0.4 s) Figure 1.1: Pictorial representation of pressure and flow over the cardiac cycle.
The geometry of the vessel is also another important aspect of the flow. The curvature of the aortic arch is non-planar, with the radius of the vessel 0.3 times the size of its radius of curvature [11]. Mathematically, the simplest such curve is that of a helical pipe. Assuming the torsion to be small, one could consider the aortic arch as a curved pipe of finite curva- ture or even weak curvature. This latter assumption, provides a significant mathematical simplification though perhaps is not the most suitable, given that the aortic arch is highly curved. Furthermore, the walls of the vessel are compliant. However, as the diameter in large arteries only varies by up to 5% over the cardiac cycle [57], it is not unreasonable to model the aorta as a rigid pipe.†
It follows from the above considerations that suitable curved-pipe models for the aortic arch, of varying complexity, can be considered. Importantly, the analysis of the different idealised problems can provide physical insight into the underlying mechanisms and effects of individual components in the flow. To conclude the discussion on the physical aspects of this problem a very brief overview of some of these is given. The focus of which is to highlight the essential differences of the characteristic flow in each model. Much of the information for this is drawn from the review by Pedley [68].
Steady, fully-developed flow in a rigid, weakly curved pipe. The first theoretical study of
†A recent analytic study on compliant curved pipes was completed by Payvandi [66], which also includes an extensive review of previous analytic and numerical work. Chapter 1. Introduction 17
flow in a curved pipe was completed by Dean [21, 22]. He showed that the flow depends on 2 a single dimensionless parameter, known as the Dean number, K = (a/288L) (aw0/ν) where a is the radius of the pipe, L is the radius of curvature, ν is the kinematic viscosity and w0 is the maximal velocity in a straight pipe driven by the same pressure gradient. He expanded the velocity field in powers of the Dean number. Characteristically, in addition to the down-pipe stream there is a secondary flow in the cross-section of the pipe. This occurs as the pressure gradient induced to balance the centrifugal force generated by the curvature of the pipe is smaller near the wall. Consequently, the fluid in the core is swept to the outside bend and the fluid near the wall to the inside bend. Therefore, the secondary flow takes the form of two counter-rotating vortices. This coupled with the main down-pipe stream results in a helical motion of the fluid in the upper and lower halves of the pipe. The contour plot is depicted in Figure 1.2. Some of the effects of this secondary flow have been discussed previously, in the context of industrial applications. More details of this problem will be given in Section 1.2.
x
Figure 1.2: Sketch of streamlines of the azimuthal and secondary velocity in curved pipes.
Unsteady, fully-developed flow in a rigid, weakly curved pipe. Lyne [49], extended Dean’s work to flow driven by a high-frequency sinusoidal pressure gradient using matched asymp- totics. There are three parameters which characterise unsteady flow in a curved pipe: the Dean number, as in the steady case, the Womersley number α = (ωa2/ν)1/2, where ω is the frequency of the oscillation and; the secondary streaming Reynolds number defined as 1.1 Motivation - the physical problem 18
2 Rs = w0a/Lων, which acts as a Reynolds number for the steady flows that are generated in the secondary circulation. Lyne considered a zero mean pressure gradient, so that the Dean number vanishes. In the limit of large α (> 12.9), for both small and large streaming Reynolds number, he found the flow to be composed of two regions: (i) the boundary layer, in which viscous effects dominate and the secondary flow is a vortex driving fluid from the outside to the inside of the bend, similar to vortex found in the flows driven by steady pressure gradient; (ii) the core region, which is essentially inviscid, where the secondary flow is a vortex rotating from the inside to the outside of the bend formed by the drag on the core fluid of the vortex in the boundary layer. This four-vortex structure is sketched in Figure 1.3.
Figure 1.3: Sketch of the streamlines of the secondary velocity in curved pipes as found by Lyne [49].
For α < 12.9, Lyne postulated that a two-vortex, Dean-like flow would exist. This hy- pothesis appears to be confirmed by the experimental work of Bertelsen [8] and Munson [61].
Other important analytical work on this problem are that of Blennerhasset [9] and Smith [75]. Blennerhasset considered the regime in which the magnitude of the secondary stream- ing found by Lyne is comparable to the secondary flow found by Dean, K R , in the ≤ s high Wormesley number limit. For small K he found the secondary flow was towards the inside wall. For large K he found the secondary flow was towards the outside wall. Smith studied several cases which arise when Rs is of order unity and one of the other parameters α and K takes a large or small value. Chapter 1. Introduction 19
Unsteady / steady, fully-developed flow in a rigid, finitely curved pipe. The studies dis- cussed above considered weakly curved pipes. For pipes of finite curvature, Siggers & Wa- ters considered the flow driven by a steady [73] and an unsteady pressure gradient [74]. For small and large parameter values, curvature and Dean number, solutions were determined by asymptotic analysis, whilst numerical methods were employed for the intermediate pa- rameter values. The features of this flow were qualitatively similar to the weak curvature limit however, the effects of finite curvature leads to significant quantitative difference. For instance, in the steady case, they found that there was a significant increase in the wall shear stress at the inner wall compared to the weakly curved pipe predictions.
Unsteady / steady, fully-developed flow in a rigid, helical pipe. Relatively recently, the effect of torsion has been considered by Zabielski & Mestel, who considered flow driven by a steady [97] and an unsteady pressure gradient [98] in a helical pipe. Notably, in the former study, they found that torsion caused a transition from a symmetric one-vortex secondary flow, to a symmetric two-vortex Dean-like flow. The latter study included a study of physiological pressure pulse, in addition to the more common sinusoidal pressure gradient of Lyne. Significantly, they found that torsion may result in higher shear stresses localised at the inner wall when compared with toroidal pipe flows. They suggest that the helical geometry may play a beneficial role in the macro-circulation and so inhibit the formation of atherosclerotic lesions.
This thesis is concerned with steady, fully-developed flow through weakly curved pipes, driven by a constant pressure gradient, which, as discussed, can be considered the simplest model for the aortic blood flow. Notwithstanding any reservations about its applicability in this respect, it is an interesting problem worthy of study in its own right. Indeed, the work presented within this thesis is primarily motivated by theoretical considerations which are now examined.
1.2 Motivation - the theoretical problem
Incompressible, steady, fully-developed flow in curved pipes is a formidable problem. Over 90 years of study have highlighted some interesting aspects of the flow, some of which are not yet entirely resolved. A review of previews work is given in this section, highlighting some of those problems which form the main incentive here. Much of the information for this section is drawn from the review by Berger [7]. 1.2 Motivation - the theoretical problem 20
1.2.1 Dean Equations
The governing equations for steady, fully-developed flow in curved pipes were derived by Dean [21, 22] and now bear his name. For completeness, the details of this derivation are now presented.
Consider a circular pipe with fixed radius a and radius of curvature L described by the orthogonal coordinate system (r,θ,φ), as shown in Figure 1.4, with:
x =(r sin θ + L) cos φ, y = r cos θ, z =(r sin θ + L) sin φ, (1.1) where r denotes the distance from the centre of the pipe, θ is the angle between the radius vector and the plane of symmetry and Lφ is is the down-pipe distance which increases in the direction of flow.
The velocity u = (u,v,w); where w is the azimuthal velocity normal to the cross-section while u and v are the radial and angular velocity components in the pipe cross-section respectively (as shown in Figure 1.4).
Figure 1.4: Coordinate system for curved pipe with circular cross-section
The flow is assumed steady and incompressible. The relevant continuity and Navier-Stokes equation are thus:
u =0, (1.2) ∇ p u u = + ν 2u, (1.3) ∇ −∇ ρ ∇ Chapter 1. Introduction 21 where p is the pressure, ρ is the density and ν is the kinematic viscosity. The flow is fully developed, so that u is independent of φ. In the coordinate system above the continuity and momentum equations reduce to:
∂u u u sin θ 1 ∂v v cos θ continuity: + + + + =0, (1.4) ∂r r L + r sin θ r ∂θ L + r sin θ
∂u v ∂u v2 w2 sin θ r-momentum: u + ∂r r ∂θ − r − L + r sin θ ∂ p 1 ∂ cos(θ) ∂v v 1 ∂u = ν + + , (1.5) −∂r ρ − r ∂θ L + r sin θ ∂r r − r ∂θ
∂v v ∂v uv w2 cos θ θ-momentum: u + + ∂r r ∂θ r − L + r sin θ 1 ∂ p ∂ sin θ ∂v v 1 ∂u = + ν + + , (1.6) −r ∂θ ρ ∂r L + r sin θ ∂r r − r ∂θ
∂w v ∂w uw sin θ vw cos θ φ-momentum: u + + + ∂r r ∂θ L + r sin θ L + r sin θ 1 ∂ p ∂ 1 ∂w w sin θ = + ν + + −L + r sin θ ∂φ ρ ∂r r ∂r L + r sin θ 1 ∂ 1 ∂w w cos θ + + . (1.7) r ∂θ r ∂θ L + r sin θ
p As (u, v, w) are assumed independent of φ, it follows from (1.7) that ρ must be of the form φf1 (r, θ)+ f2 (r, θ) and then from (1.5) and (1.6) that f1 (r, θ) must be a constant.
The continuity equation (1.4) is satisfied by the streamfunction ψ (r, θ) such that:
1 ∂(hψ) 1 ∂(hψ) = u, = v, (1.8) hr ∂θ − h ∂r where h = L + r sin(θ).
The mean axial pressure gradient is
1 ∂ p G = , (1.9) −L ∂φ ρ ρ 1.2 Motivation - the theoretical problem 22 where G is a constant.
These identities are substituted into equations (1.5), (1.6) and (1.7) and the pressure terms are eliminated from equations (1.6) and (1.7) by cross-differentiation. The governing equa- tions become:
∂(hψ) ∂ ∂(hψ) ∂ 2w ∂w ∂w νr 4ψ = 2ψ + sin θ r cos θ , ∇ ∂r ∂θ − ∂θ ∂r ∇ h ∂θ − ∂r 1 ∂(hψ) ∂w ∂(hψ) ∂w w sin θ ∂(hψ) r cos θ ∂(hψ) G ν 2w = , ∇ hr ∂r ∂θ − ∂θ ∂r − hr h ∂θ − h ∂r − ρ where
1 ∂ r ∂(h f) 1 ∂ 1 ∂(h f) 2f = + . ∇ r ∂r h ∂r r2 ∂θ h ∂θ 1.2.1.1 Non-dimensionalisation & boundary conditions
The following non-dimensional variables are introduced:
r ψ w a h rˆ = , ψˆ = , wˆ = , δ = , h = , a ν ω0 L L where ω0 is the maximum down-pipe velocity in a straight pipe with circular cross-section driven by the same pressure gradient and ν is the kinematic viscosity.
The governing equations are then reduced to (dropping the hat notation for convenience):
1 ∂(hψ) ∂ ∂(hψ) ∂ w sin θ ∂w ∂w 4ψ = 2ψ + 576K cos θ , ∇ r ∂r ∂θ − ∂θ ∂r ∇ h r ∂θ − ∂r 1 ∂ψ ∂w ∂ψ ∂w δw sin θ ∂(hψ) r cos θ ∂(hψ) 2w = C, ∇ r ∂r ∂θ − ∂θ ∂r − hr h ∂θ − h ∂r −