Steady-State Thermoelastic Analytical Solutions for Insulated Pipelines

1Department of Structures for Engineering and Architecture, University of Napoli Federico II, Napoli, Italy 2Interdisciplinary Research Center for Biomaterials, University of Napoli Federico II, Napoli, Italy 3Department of Fire Watch, Public Rescue and Civil Protection, Italian Ministry of Interior, Roma, Italy 4Department of Chemical, Materials and Production Engineering, University of Napoli Federico II, Napoli, Italy


Introduction
In the last years, a growing demand for insulated pipes operating at higher temperatures has addressed a need of insulation materials able to withstand thermal degradation and physical stress.As a consequence, the design of piping, with particular attention on the thermomechanical properties of the adopted materials, has become an important aspect in any energy consuming system, due to the considerable impact of the insulation arrangement and sizing on the overall performance of the structure.Actually, the design of pipelines is usually based on either worked before or educated estimates and is deeply influenced by both hardware and energy costs.Oversized pipes are designed to preserve thermal energy, and adequate insulations are chosen to achieve both low thermal conductivity and inertia, in order to reduce heat loss from hot surfaces and heat gain in refrigeration systems.In fact, either inadequate thickness or deterioration of existing insulation causes high energy consumptions, so that retrofitting or reinsulation techniques, strictly related to the development of higher performances at lower prices insulating materials, are becoming a very attractive energy saving method.In this framework, multilayer insulated pipes could be a suitable alternative, in which different materials can be used to enhance energetic performances of pipelines.De facto, multilayered insulated pipelines can be considered as laminate composites.Laminate composites and socalled functionally graded material structures (FGMs) have been deeply studied thanks to their capability of working in high-temperature environments and many research works have been carried out for characterizing spherical, plated, and cylindrical shapes FGMs by means of both analytical and numerical approaches [1][2][3][4][5][6][7].
In particular, by adopting an analytical approach, different scientific studies have been devoted to investigate the effects of nonlinear constitutive properties and nonhomogeneities on the response of cylindrical FGMs subject to nonlinear distribution of temperature along the radius.Eraslan [8] developed the analytical solutions of nonuniform heat-generating composite tubes with fixed ends, subject to thermally induced axisymmetric elastoplastic deformations, calculating the results as a consequence of nonlinearly hardening properties.Instead, Shao [9] derived analytical solutions of a circular hollow cylinder composed of different homogeneous fictitious layers in the radial direction, finding mechanical and thermal stresses for the two-dimensional thermoelastic problems.Fraldi et al. [10] showed the exact analytical solutions for the elastic response of a solid circular cylinder composed of the assembly of a central core and  surrounding hollow phases, all made of different homogeneous elastic materials; under de Saint Venant-like load conditions, they produced overall elastic relationships between generalized stresses and strains in cases of axial force, torque, bending, and shear, also registering the effects of Poisson ratios on the overall stiffness.Moreover, Fraldi et al. [11], in hypothesis of no-decaying of selected mechanical quantities, obtained a special form of the biharmonic Love's function, as expression of the radius and the coordinate along the axis.Eraslan and Akis [3], in the framework of small deformation theory, obtained plane strain analytical solutions for a functionally graded elastic-plastic pressurized tube, making reference to Tresca's yield criterion, showing that the elastoplastic response of the pressurized tube is significantly affected by the material nonhomogeneity.By adopting Green's function approach, Kim and Noda [6] solved the twodimensional unsteady temperature problem, determining the associated thermal stresses in an infinite hollow cylinder with radially dependent properties.Further studies by Jabbari et al. [7] derived analytical solutions for one-dimensional steady-state thermoelastic circular hollow thick cylinders and, by assuming the temperature distribution and material properties to be functions of the radius with a power law distribution, obtained the solution of the heat conduction and Navier equation, while Liew et al. [12] determined analytical solutions of a circular hollow cylinder by a novel limiting process employing the solutions of homogeneous circular hollow cylinders.Also, several studies have focused the attention on the analysis of composite pipelines under combined thermal and mechanical conditions, with the aim of highlighting both specific aspects of interest for practical engineering applications [13][14][15][16] and theoretical insights [17][18][19].
In this paper, by using a multilayered approach based on the theory of laminated composites, a steady-state thermoelastic analytical solution for a multilayer hollow cylinder, composed of an arbitrary number of phases and subject to both radial pressure and temperature gradients, is proposed.Successively, by assuming the material properties to be piecewise radially varying (homogeneous in each layer) and temperature-independent, parametric analyses and analytical solutions for a three-layered hollow cylinder composed of steel, insulating coating, and polyethylene jacket are presented.The results are shown by varying Young's moduli, Poisson's ratios, thermal conductivity, and linear expansion coefficients of the constituent materials.In order to localize the onset of plasticity and following the Hencky-von Mises criterion, the maximum equivalent stress has been finally determined both in the steel phase and in the insulate coating.At the end, a numerical example is reported considering the insulate coating composed of expanded polyurethane, laminate glass, and syntactic foam.

Basic Equations for the Steady-State Problem
A hollow multilayered cylinder constituted by  phases with finite length  has been considered (Figure 1(a)).The external and internal radii of the multilayer cylinder and the radius at interface between the generic th and ( + 1)th phases have been denoted by  () ,  (0) , and  () , respectively.The mechanical and thermal properties of each layer have been assumed to be homogeneous and isotropic and are denoted with apex ().A thermal gradient has been considered across the pipe walls, with external and internal values of, respectively,  ext and  int , and constant pressure values have been applied both on the outer ( ext ) and on the inner surfaces ( int ), that is, at  =  () and  =  (0) , respectively.By assuming a cylindrical coordinates system {, , }, if the hollow cylinder is subjected to radial temperature variation and radial uniform pressure, one can seek the displacement as reduced to the sole radial and axial (along -direction) components in the following form, the temperature becoming a function of the sole variable  at each th layer, so that where apexes 1, 2, . . .,  denote the pipe layers and  0 represents the constant axial strain shared among the phases [11].Therefore, the nonvanishing strain components take the form Similarly, considering each phase as isotropic, the nonvanishing stress components can be written as Insulate coating (2) Polyethylene jacket (3) Steel pipe (1) R (2)   R (3)   T e (b)  ()   = 2 ()  0 +  () ( () , +  −1  ()  +  0 ) − (3 () + 2 () )  () ( () −   ) , ∀ ∈ {1, 2, . . ., } , where  () ,  () ,  () , and  () are the two Lamé elastic moduli, the thermoelastic coefficients, and temperature field for the th layer, respectively.By applying the hypothesis of axial-symmetric and in absence of body forces, the equilibrium equations reduce to the sole nontrivial one: By substituting the strain-displacement relations (2) in the stress-strain relations (3) and thus in the equilibrium equation (4), the displacements in each phase become the unknown functions to be determined.If the Lamé coefficients are expressed as functions of elastic moduli  () and ] () , by invoking the well-known following relations, the displacements formulation of the equilibrium equations allows reducing the problem at hand to one ordinary differential equation: , = 2 ()  () , , ∀ ∈ {1, 2, . . ., } , where the constant In order to impose both equilibrium and compatibility at the boundary surfaces between two generic adjacent phases, under the hypothesis of perfect bond at the cylindrical interfacial boundaries (no delamination or friction phenomena), the generic solution for a functionally graded circular cylinder constituted by  arbitrary hollow phases can be set.In particular, the following boundary conditions have been established in terms of displacements at the interfaces and the equilibrium of stresses at the generic interface requires having Mathematical Problems in Engineering Also, equilibrium equations for the tractions at the inner and the outer cylindrical boundary surfaces are given by where  ext and  int are the pressure applied on the inner and the outer surfaces of the multilayered cylinder, respectively.It is worth highlighting that the choice to assume a displacement field in which the axial strain  0 is constant and common to all the phases automatically guarantees the compatibility of the displacement along the -direction at the interfaces, also ensuring vanishing antiplane shear stresses  ()   and, by virtue of the particular form of the other displacement functions, torsionless deformation and stress regimes; that is,  ()  = 0.As a consequence of this choice for the axial strain, two possibilities can be taken into account, say first in which  0 = 0 and another (complementary) one in which, dually, the axial resultant  emerging from any overall cylinder cross section along the -direction is set to be equal to zero.In the first case that is the case considered in the present work the problem reduces to plane strain and the resultant  will be identified as the reaction that allows the deformation to remain plane through different values of stresses  ()   generated within each phase.On the contrary, the same general form assumed above for the displacements could be exploited to replicate the dual case in which the axial elongation (or contraction)  0 is chosen to give  = 0.
As anticipated above, without loss of generality with respect to the possibility of reproducing both the cases described above, in what follows the condition  0 = 0 is set and hence an axial force , whose magnitude does not depend on , can be found once the solutions in terms of displacements and related stresses will be completely defined; that is, Hypothesizing axial-symmetric load conditions for each phase, the steady-state conduction equation can be written as At the interfaces between the phases, the temperature and heat flux are equal, so that the following conditions can be written: , where  () is the thermal conductivity coefficient of the phase.
Similarly, on the inner and the outer surfaces, the temperature is equal to  ext and  int , respectively,

Analytical Solution in Closed-Form for Multilayered Cylinder in Plane Strain Subject to Radial Temperature Variation and Uniform Pressure
By integrating ( 6), the displacements solution in each phase of a multilayered cylinder can be found in closed-form as follows: where  () 1 and  () 2 are integration constants to be determined.By integrating Fourier's equation reported in (11), the temperature function for the steady-state problem in each phase takes the form where  () 1 and  () 2 are parameters to be specialized through the boundary conditions.Thus, the heat flux in each phase is given by and substituting the temperature function ( 15) in ( 14), the explicit expression of the displacement function can be obtained: ∀ ∈ {1, 2, . . ., } .
In order to solve the first algebraic system (i), it is easy to determine the coefficients  () 1 ,  () 2 ∀ ∈ {2, 3, . . ., }, as function of the two coefficients of the first phase:  (1)  1 ,  (1)  2 .Thus, by solving the algebraic system (25), the following relations can be obtained: By substituting (28) into the algebraic system (26), setting  equal to , the constants  (1)  1 and  (1)  2 can be then determined, as reported below: where  = ( (1) / log Finally, the solution in closed-form of the algebraic system (i) is written as follows: and the temperature function in each phase can be explicitly found as In order to solve the second algebraic system (ii), the subsystem constituted by the equilibrium and compatibility conditions ( 22)-( 23) is considered: where the vectors L = [L (1) , L (2) , . . ., L () ]  are characterized by the following subvectors: in which the vector A () and the matrix Γ () are given by and X = [X (1) , X (2) , . . ., X () ]  collects the unknowns subvectors X () , as reported below: The matrix Q results are then composed of the following submatrices: Mathematical Problems in Engineering 7 where the generic matrices B ()  and B (+1)  , given by are (2 × 2) matrices with nonzero determinants, whose components have been already given above.The determinant of the matrices (37) is in particular written as follows: However, in force of the special form of the matrix Q, the algebraic system (32) can be reorganized as B (2)  1 X (2) = B (1)  1 X (1) + L (1) , 2 X (2) + L (2) , . . .
and, by applying an in-cascade procedure, it can be finally obtained where Φ () and Ψ () are matrix and vector, respectively.The explicit expressions of Φ () and Ψ () are given below: By means of (40) and (41), the generic unknowns subvector X () can be written as a function of the transferring matrix Φ () , the vector Ψ () , and the unknowns subvector X (1) .By imposing the two boundary conditions described by the equations obtained above, the differential problem reduces to an algebraic one in which only two coefficients, collected in X (1) and related to the first phase, have to be determined.Therefore, in order to find the two unknowns collected in X (1) , the boundary conditions (24) can be written in matrix form.In particular, by applying (40) for  = , the following relationship is obtained: Then, the boundary conditions (24) become where the matrix P and the vector L  are given by P 1 and P 2 being two vectors, dot denoting the standard scalar product, and  1 ,  2 being two scalars, whose explicit expressions are ,  1 = −Ω (1)   +  (1) [ (1)  1 (log Therefore, by inverting all the 2 ×  unknown coefficients, the unknown parameters are finally found out: By substituting the relationships ( 46) and ( 30) in (17), the explicit analytical expression of the solution in terms of displacements for each phase of the multilayer hollow cylinder can be obtained.

Radius and Thickness for Insulated Pipelines according to European Standards EN 253
Generally, the industrial insulate pipeline is composed of three phases: steel pipe, insulate coating, and external casing.The minimum dimensions of thickness of the steel pipe and casing are prescribed in European Standards EN 253, as function of nominal outside diameter.By fitting the values given by EN 253, the following expression describes the minimum values of the thickness of the steel pipe, as function of the inner radius Similarly, the minimum value of the thickness  (3) of the casing, as function of maximum radius of the casing  (2) , is reported below: By applying the relationships ( 47) and ( 48), the geometrical parameters of the insulate pipeline depend on two parameters  (0) and  (2) only, as reported below: = 3 ⋅ 10 −3 + 1.0165 (0) +  (2) ,  (3) = 5.5438 ⋅ 10 −3 + 1.03134 (0) + 1.0146 (2) . ( The inner radii of the steel pipe  (0) and insulate coating  (2)  are usually found to vary within the following ranges: (2) ∈ [0.0345, 0.6875 m] . (50) By applying the relationship (49), if the inner radius  (0) is prescribed, the thickness  (2) must satisfy the inequalities: 0 ≤  (2) ≤ 0.078 for  (0) = 0.597, 0.0227 ≤  (2) ≤ 0.6757 for  (0) = 0.00865. (51) The domain of the parameters  (0) and  (2) , satisfying the values given by EN 253, is reported in Figure 2.

Parametric Analysis of an Industrial Insulated Pipeline Composed of Three Phases
In this section, an industrial insulated pipeline has been modelled by means of a multilayered solid composed of three hollow cylinders, as showed in Figure 1(b).The materials characterizing the insulated pipeline are steel (phase 1), insulated coating (phase 2), and polyethylene (phase 3), adopted to protect the insulation.Accordingly to European Standards,   (2) .Table 1: Mechanical and thermal parameters of steel and polyethylene.

Steel pipe
Polyethylene jacket the inner radius and the thickness of the pipeline and the polyethylene jacket are fixed by applying the limitation reported in the EN 253.
The inner radius and thickness of the pipeline and the polyethylene jacket have been set to  0 = 0.20 m and  (2) = 0.20 m, for the case at hand.By applying the relationships (47), (48), and (49), the other geometrical parameters of the multilayered cylinder have been obtained and detailed below: Also, mechanical and thermal properties of steel and polyethylene are reported in Table 1.
(ii) Young's moduli and linear thermal expansion coefficient have been parametrically varied, prescribing both Poisson's ratio and the thermal conductivity coefficients.
In order to localize the onset of plasticity, in the case of planar isotropy and nonhomogeneity in radial direction, the equivalent stress based on the Hencky-von Mises criterion has been chosen, in the form recalled below: The following dimensionless parameters for the maximum absolute value of nondimensional equivalent stress have been also taken into consideration: The effects of Poisson ratio and Young modulus variation on the maximum value of nondimensional equivalent stress are shown in Figure 3, when an insulated pipeline is subject to thermal gradient, load case (a), in the steel (phase 1), in the insulated coating (phase 2), and in the polyethylene jacket (phase 3).
It is worth noticing that, by increasing Young's modulus of the insulate coating, the maximum values of the equivalent stress increase in the steel pipe (Figure 3 affected by the Young moduli as they increase.Moreover, higher Poisson's ratios of insulate coating increase the maximum values of the equivalent stress in each phase and, in the particular case in which the insulated coating is composed of auxetic material with negative Poisson's ratio, the maximum equivalent stress significantly reduces in each phase.
Similarly, the results, in terms of the maximum values of the equivalent stress in each phase, obtained by varying the Young modulus and the linear thermal expansion coefficient, are shown in Figure 4.
At fixed value of the thermal expansion coefficient, by increasing Young's modulus of the insulate coating, the equivalent stress increases in the steel pipe and remains practically constant in both the polyethylene jacket and the insulate coating.Moreover, by increasing the linear thermal expansion coefficient of the insulate coating, the maximum values of the equivalent stress increase in each phase.
By considering the load case (b), a parametric analysis has been instead conducted with the aim of studying the effects of Poisson's ratio and Young's modulus variation on the mechanical response of an insulated pipeline subject to internal radial pressure.In particular, the maximum values of nondimensional equivalent stress in the steel, in the insulated coating and in the polyethylene jacket, are shown in Figure 5.
By increasing Young's modulus in the insulate coating, the maximum equivalent stress decreases in the steel pipe while, by decreasing Poisson's ratio in the insulate coating, the maximum values of the equivalent stress decrease in the steel pipe up to reach lowest values as Poisson's ratios tend to negative (auxetic) values (Figure 5(a)).A complementary behaviour is instead observed in the insulated coating phase (Figure 5(b)).
Finally, by increasing Young's modulus in the insulate coating, the maximum equivalent stress decreases in the polyethylene jacket while, by decreasing Poisson's ratio in the insulate coating, the maximum values of the equivalent stress increase in the polyethylene jacket (Figure 5(c)).

Numerical Example of an Insulated Pipeline Subject to Temperature Gradient
In the present section, a numerical example, an insulated pipeline subject to temperature gradient (jump) equal to 120 ∘ C and constituted by three phases (steel pipe, insulate coating, and polyethylene jacket), is reported.The nondimensional equivalent stress, calculated by applying formulas (54), has been evaluated for three types of materials characterizing the insulate coating: (1) expanded polyurethane, (2) laminate E ( 2 )  = 1 0 0 0 0 M P a E ( 2 )  = 4 0 0 0 M P a E ( 2 )  = 2 0 0 0 M P a E ( 2 )  = 5 0 0 M P a E ( 2 )  = 1 0 0 M P a glass, and (3) syntactic foam.The mechanical and thermal properties of the adopted materials are reported in detail in Table 2.
Along the steel pipe phase radius (Figure 5(a)), if the insulate coating is constituted by laminate glass (Case 2), the nondimensional equivalent stress assumes values smaller than the other cases (Cases 1 and 3), due to the fact that the linear thermal expansion coefficient of laminate glass is smaller than those of expanded polyurethane and syntactic foam.On the other hand, along the insulate coating phase radius (Figure 5(b)), if the insulate coating is constituted by expanded polyurethane (Case 1), the nondimensional equivalent stress assumes values greater than the other cases (Cases 2 and 3) because Young's modulus of expanded polyurethane is smaller than those of laminate glass and syntactic foam, while, moving along the polyethylene jacket radius (Figure 5(c)), if the insulate coating is constituted by laminate glass (Case 2), the nondimensional equivalent stress assumes values smaller than the other cases (Cases 1 and 3) because the linear thermal expansion coefficient of laminate glass is smaller than those of expanded polyurethane and syntactic foam.

Conclusions
In the present work, analytical solutions and numerical results for a class of multilayered cylinders under combined thermomechanical conditions have been obtained.1.25 ⋅ 10 −4 1.9 ⋅ 10 −5 5.0 ⋅ 10 −5 The closed-form thermoelastic solution has been in particular found first for a generic FGM hollow cylinder with  layers and thus for a multilayer hollow cylinder composed of three phases, steel pipe, insulating coating, and polyethylene jacket, and subject to two prescribed loading conditions.Parametric analyses have been conducted by varying mechanical properties of the adopted materials, by making reference to the Hencky-von Mises criterion to localize the possible onset of plasticity.The results have shown that when the insulated pipeline is subject to temperature gradients, the maximum equivalent stress reduces in steel pipe, coating, and jacket, if the linear thermal expansion coefficient of insulate coating assumes values close to the linear thermal expansion coefficient of the steel, being thus possible to significantly reduce the maximum equivalent stress in the pipeline and avoid failure by utilizing the insulated coating composed of auxetic material (with negative Poisson's ratio).Moreover, when the insulate pipeline is subjected to radial pressure, insulated coating with negative Poisson's ratio shows reduced values of the maximum equivalent stress in steel phase only, but the values in the other two phases result generally increased.Finally, a numerical example related to a case of practical engineering interest, that is, a hollow cylinder composed of three different insulation materials and thicknesses according to EN 253, has been presented, the results showing that
(a) Pipeline subject to temperature gradient between the internal and external surfaces Δ =  int −  ext .(b) Pipeline subject to internal pressure, with parametrically varying Poisson's ratios and Young's moduli.

Figure 3 :
Figure 3: Maximum value of nondimensional equivalent stress in the steel (phase 1: (a)), in the insulated coating (phase 2: (b)), and in polyethylene jacket (phase 3: (c)) in the case of insulate pipeline subjected to temperature gradient.

Figure 4 :
Figure 4: Maximum value of nondimensional equivalent stress in the steel (phase 1: (a)), in the insulated coating (phase 2: (b)), and in polyethylene jacket (phase 3: (c)) in the case of insulate pipeline subjected to temperature gradient.

Figure 5 :
Figure 5: Maximum value of nondimensional equivalent stress in the steel (phase 1: (a)), in the insulated coating (phase 2: (b)), and in polyethylene jacket (phase 3: (c)) in the case of insulate pipeline subjected to internal radial pressure.

Figure 6 :
Figure 6: Equivalent stress [MPa] along the radius in the case of insulate pipeline subjected to temperature gradient in the steel (a), in the insulate coating (b), and in the polyethylene jacket (c).Case 1: expanded polyurethane, Case 2: laminate glass, and Case 3: syntactic foam.