# Modelling of Creep and Stress Relaxation Test of a Polypropylene Microfibre by Using Fraction-Exponential Kernel

Authors: Andrea Sorzia
Journal: Modelling and Simulation in Engineering
 (2016)

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## Abstract

A tensile test until breakage and a creep and relaxation test on a polypropylene fibre are carried out and the resulting creep and stress relaxation curves are fit by a model adopting a fraction-exponential kernel in the viscoelastic operator. The models using fraction-exponential functions are simpler than the complex ones obtained from combination of dashpots and springs and, furthermore, are suitable for fitting experimental data with good approximation allowing, at the same time, obtaining inverse Laplace transform in closed form. Therefore, the viscoelastic response of polypropylene fibres can be modelled straightforwardly through analytical methods. Addition of polypropylene fibres greatly improves the tensile strength of composite materials with concrete matrix. The proposed analytical model can be employed for simulating the mechanical behaviour of composite materials with embedded viscoelastic fibres.


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## Body

## 1. Introduction

Fibre-reinforced composite materials consist of fibres with high strength and elastic modulus embedded in a matrix to produce a combination of properties that cannot be achieved by single constituents. Usually, fibres are the principal load-carrying members, while the surrounding matrix keeps them in the desired location and orientation. The matrix acts as a load transfer medium between fibres and plays a number of useful functions, for example, protecting the fibres from environmental damage. Fibres may be made up of various materials, such as steel, polymer, glass, or carbon, whereas polymer, metal, or ceramic can be chosen for the matrix material.Fibre-reinforced polymer composites are probably the most important and widespread fibre-reinforced materials used for commercial and industrial applications. This is due to the combination of their low density, strength-weight ratios, and modulus-weight ratios that make them more attractive than many traditional metallic materials [1].A classic example of fibre-reinforced composite used in civil engineering is Fibre-Reinforced Concrete (FRC), widely adopted for industrial pavements, tunnel linings, marine structures, earthquake-resistant structures, and plate and slab foundation [2]. In FRC composites, fibres are commonly added to concrete mixture in random disposition and short cuts in order to increase the cracking behaviour of concrete, thus transforming concrete from brittle into a ductile material [3]. However, there are composite materials in which fibres are aligned along particular directions, as it occurs in FRP frame elements (these composites can be studied by adopting, for instance, the approaches proposed in [4, 5]).Recently, the use of macro synthetic fibres made of polymeric materials has been proposed for structural purposes [6, 7]. Experimental tests performed by Lanzoni et al. [8] show that the addition of polypropylene-based draw-wired fibres significantly improves crack resistance of the concrete mixture and enhances toughness and durability of FRC structural elements. Fibres could be found in interesting applications as an additive to improve concrete under aggressive environments (the mechanical behaviour has been studied under high thermal loads also [9, 10] and nuclear radiation [11]). However, particularly in such harsh conditions, a wide class of additives can be inserted at the mixing stage (like fly ash) to increase resistance of the concrete mixture [12].Ductility and flexural strength of FRC are defined by energy-dissipation mechanisms during the pullout of the fibres that occurs in the opening propagating cracks [13, 14].Pullout of the fibres begins after cracking the concrete matrix (for the stress and strain localizations at the crack tip, see, e.g., [14–17]) and ceases with the complete extraction of the fibres and its evolution depends on the bonding between fibre and matrix [18, 19]. Nevertheless due to their chemical inertness, polypropylene (PP) synthetic fibres have poor adhesion to the cement matrix with respect to other kinds of fibres. However, special surface nanotreatment can actually increase the adhesion properties between concrete and synthetic fibres, as shown by Di Maida et al. [3]. In this case, PP fibres may experience significant loading and consequently the viscous deformations of the composite material may considerably increase (for time-dependent effects in concrete structures see [20–22]). A single fibre can be studied as an embedded cylindrical body or a viscoelastic circular nanobeam in frictional contact with the cement matrix under axial tensile load (e.g., [23–25]).Another application of synthetic fibres in civil engineering is the fibre-reinforced polymer (FRP) composites for reinforcement and retrofitting of concrete and masonry members, with applications in new buildings as well as for strengthening and/or rehabilitation of existing (prestressed as well as nonprestressed) structural members of both prefabricated and cast-in-place frames. FRP reinforcement consists in strengthening fibres applied to structural elements by a cementitious or polymeric-based layer. The mechanical performances of such systems can be assessed by solving the contact problem between two bounded layers [26–28] where the adhesive layer is a fibre-reinforced composite material [29] or, in a simpler way, as a fibre-reinforced Kirchhoff plate [30].This work presents a creep and stress relaxation test performed over a PP synthetic fibre used for FRC. Creep is a time-dependent deformation of a viscoelastic material under the application of a constant stress at a constant temperature. Relaxation is the counterpart of creep, namely, a time-dependent stress of a viscoelastic material under the application of a constant deformation at a constant temperature. Both are complex phenomena for they depend on material properties (e.g., molecular orientation and crystallinity) and external conditions (e.g., applied stress, temperature, and moisture). Moreover, the viscoelastic behaviour of PP fibres embedded in an elastic matrix complicates the modelling of creep and stress relaxation response of the composite material, which depends on many additional parameters such as concentration, aspect ratio, orientation, and, obviously, mechanical properties of PP fibres.Creep and stress relaxation tests best demonstrate the viscoelastic characteristics of a polymeric solid. In creep test, a constant stress is maintained on a specimen while its deformation is monitored as a function of time, and deformation increases with time. In stress relaxation test, a constant deformation is maintained while the stress on the specimen is monitored as a function of time, and stress decreases with time. Typical creep and stress relaxation diagrams exhibit an instantaneous elastic response followed by a delayed time-dependent response [1].Over the experimental creep and stress relaxation tests performed, this paper proposes an analytical model to fit these experimental curves. The model uses fraction-exponential kernel in the viscoelastic operator and was proposed, for the first time, by Scott Blair and Coppen [31, 32] and Rabotnov [33] independently.The classical viscoelastic constitutive models represented by a combination of dashpots and springs are usually adopted for simulating creep behaviour of composite materials. However, the simplest ones (Maxwell and Kelvin-Voight) are not sufficiently flexible to match experimental data for real materials. The more complex ones, obtained from combination of different Maxwell and Kelvin-Voight models, require instead many parameters and do not allow obtaining inverse Fourier or Laplace transforms in closed form [34, 35]. Therefore, in the 50s of the last century, a viscoelastic stress-strain relation based on fractional derivative has been proposed. The fractional derivative model (FDM) is more flexible and requires a smaller number of parameters, so that their calibration is considerably simpler. The flexibility is due to the order of derivatives which can vary to obtain a constitutive law suitable for the considered material. In 1948 Rabotnov [33] suggested to use fraction-exponential operators that can describe experimental data of real materials with sufficient accuracy and allows one to obtain inverse Laplace transforms analytically [36]. Scott Blair and Coppen [31, 32] used fraction-exponential operators for description of viscoelastic properties of materials experimentally (see Rogosin and Mainardi [37]). Fraction-exponential functions in viscoelastic operators were used by many authors last decade. Detailed discussion can be found in the book of Podlubny [38]. Published broad surveys are, for example, [39–41].The model developed in the present paper is able to describe the creep curve of a PP fibre carefully and it allows obtaining the creep and stress relaxation test response of a fibre composite material in closed form. Moreover, the adopted fraction-exponential operators can be efficiently employed for the homogenization of synthetic FRC by extending the Maxwell scheme developed for elastic composites to viscoelastic behaviour of the constituents (e.g., [34, 42]).


## 2. Materials and Methods

### 2.1. Material and Breaking Test

The fibre consists of PP monofilament with a diameter of 0.78 mm and length of 200 mm. Since the cross section of the fibre is not perfectly circular, the diameter is an average of six measurements: Two measurements in two orthogonal directions in three points of the fibre, namely, at the middle and at both ends. To evaluate elastic Young modulus and tensile strength, tensile tests were performed on four specimens of fibres until their breakage. Each fibre was clamped at its ends and pulled by an electromechanic traction machine under displacement control.The load cell is a GALDABINI 514262 TYPE TCA, with OUTPUT sensitivity of 2 mV/V. The machine uses a 20-bit A/D converter to acquire the analogical quantities. The resolution of the load cell is 0.002 N over the entire field of use, with a capacity of 250 N. The displacement control was performed by the actuator at a rate of 40 mm/min. The average value of the breakage tensile load is 130.5 N that occurs approximately at a displacement of 10 mm, namely, at 5% of strain.The elastic Young modulusE0 (Table 1) was determined from the ratio between stress and strain. The stresses and strains were calculated based on the early stage of the experimental load-displacement curve averaged on the four fibres.Table 1
Properties of polypropylene fibre.
Diameter (mm) 0.78 Tensile strength (N/mm2) 273.0 Elastic modulusE0 at t=0 (N/mm2) 5.131 × 103 Elastic modulusE∞ at t→∞ (N/mm2) 1.959 × 103The experiments were performed at 25°C. Since the glass transition temperature of the PP is approximately −20°C [43], at room temperature PP fibres exhibit a mechanical behaviour corresponding to that of a viscoelastic material in rubbery state, that is, a time-dependent response as shown in Figure 1(b).Figure 1
(a) Tensile tests until breakage on four specimens of fibre: load versus displacement. (b) Experimental curves: creep versus time (dashed orange curve) and stress relaxation versus time (dashed cyan curve: stress scaled by 1/2000).
(a) (b)Plots of breaking tests are reported in Figure1(a). In particular, the first peak that can be observed in the curve is due to the breakage of the fibres that occurred on the clamped portion, at which followed a pullout stage until the complete detachment of the fibres. The properties adopted for PP fibre are listed in Table 1. The PP fibre was provided by the Italian company Fili&Forme® Ltd. and shown in Figure 3.


### 2.2. Creep and Relaxation Tests

The creep test was carried out on a sample of length 200 mm subject to a constant tensile force of 60 N by fixing between two clamps and measuring the displacement of the fibre over the time. The load cell is the same used for the breaking test (see Section2.1) and the speed to gain 60 N was performed at a rate of 40 mm/min. The total duration of the creep test was 15 hours needed for the fibre to achieve a (temporary) stationary value of the deformation (plateau region of the creep curve). However, it should be remarked that the deformation could further increase after 15 hours, since the maximum level of deformation is theoretically achieved at t→∞.It is worth noting that at time longer than 20,000 s the strain exceeds 5% but the fibre does not break (Figure1(b)). Conversely, the fibre under tensile test falls at a strain level equal to 5% (Figure 1(a)). This is due to the fact that the creep test was performed at a constant load of 60 N, less than one-half the ultimate tensile load of 130.5 N.Similarly, the stress relaxation test was carried out on a sample of length 200 mm subject to a constant displacement of 5 mm and measuring the tensile force over the time. The speed to gain 5 mm was performed at a rate of 40 mm/min. The total duration time was 7 hours, until the force of the fibre was almost stationary. Plots of creep and stress relaxation tests are reported in Figure1(b).Both creep and relaxation tests were performed on a single specimen.The elastic Young modulusE∞ (Table 1) was assessed based on the final stage of the experimental creep and relaxation tests by knowing the imposed constant load and displacement values at which the tests were performed. The assumed values were the averages of the obtained experimental results.


## 2.1. Material and Breaking Test

The fibre consists of PP monofilament with a diameter of 0.78 mm and length of 200 mm. Since the cross section of the fibre is not perfectly circular, the diameter is an average of six measurements: Two measurements in two orthogonal directions in three points of the fibre, namely, at the middle and at both ends. To evaluate elastic Young modulus and tensile strength, tensile tests were performed on four specimens of fibres until their breakage. Each fibre was clamped at its ends and pulled by an electromechanic traction machine under displacement control.The load cell is a GALDABINI 514262 TYPE TCA, with OUTPUT sensitivity of 2 mV/V. The machine uses a 20-bit A/D converter to acquire the analogical quantities. The resolution of the load cell is 0.002 N over the entire field of use, with a capacity of 250 N. The displacement control was performed by the actuator at a rate of 40 mm/min. The average value of the breakage tensile load is 130.5 N that occurs approximately at a displacement of 10 mm, namely, at 5% of strain.The elastic Young modulusE0 (Table 1) was determined from the ratio between stress and strain. The stresses and strains were calculated based on the early stage of the experimental load-displacement curve averaged on the four fibres.Table 1
Properties of polypropylene fibre.
Diameter (mm) 0.78 Tensile strength (N/mm2) 273.0 Elastic modulusE0 at t=0 (N/mm2) 5.131 × 103 Elastic modulusE∞ at t→∞ (N/mm2) 1.959 × 103The experiments were performed at 25°C. Since the glass transition temperature of the PP is approximately −20°C [43], at room temperature PP fibres exhibit a mechanical behaviour corresponding to that of a viscoelastic material in rubbery state, that is, a time-dependent response as shown in Figure 1(b).Figure 1
(a) Tensile tests until breakage on four specimens of fibre: load versus displacement. (b) Experimental curves: creep versus time (dashed orange curve) and stress relaxation versus time (dashed cyan curve: stress scaled by 1/2000).
(a) (b)Plots of breaking tests are reported in Figure1(a). In particular, the first peak that can be observed in the curve is due to the breakage of the fibres that occurred on the clamped portion, at which followed a pullout stage until the complete detachment of the fibres. The properties adopted for PP fibre are listed in Table 1. The PP fibre was provided by the Italian company Fili&Forme® Ltd. and shown in Figure 3.


## 2.2. Creep and Relaxation Tests

The creep test was carried out on a sample of length 200 mm subject to a constant tensile force of 60 N by fixing between two clamps and measuring the displacement of the fibre over the time. The load cell is the same used for the breaking test (see Section2.1) and the speed to gain 60 N was performed at a rate of 40 mm/min. The total duration of the creep test was 15 hours needed for the fibre to achieve a (temporary) stationary value of the deformation (plateau region of the creep curve). However, it should be remarked that the deformation could further increase after 15 hours, since the maximum level of deformation is theoretically achieved at t→∞.It is worth noting that at time longer than 20,000 s the strain exceeds 5% but the fibre does not break (Figure1(b)). Conversely, the fibre under tensile test falls at a strain level equal to 5% (Figure 1(a)). This is due to the fact that the creep test was performed at a constant load of 60 N, less than one-half the ultimate tensile load of 130.5 N.Similarly, the stress relaxation test was carried out on a sample of length 200 mm subject to a constant displacement of 5 mm and measuring the tensile force over the time. The speed to gain 5 mm was performed at a rate of 40 mm/min. The total duration time was 7 hours, until the force of the fibre was almost stationary. Plots of creep and stress relaxation tests are reported in Figure1(b).Both creep and relaxation tests were performed on a single specimen.The elastic Young modulusE∞ (Table 1) was assessed based on the final stage of the experimental creep and relaxation tests by knowing the imposed constant load and displacement values at which the tests were performed. The assumed values were the averages of the obtained experimental results.


## 3. Results and Discussion

### 3.1. Analytical Model for Creep and Stress Relaxation Curves

We wanted to fit experimental creep and stress relaxation curves with an analytical model by using fraction-exponential kernel that on one side fits carefully experimental data and, at the same time, allows analytical expression for inverse Laplace transform. Let us consider the Boltzmann convolution integral that describes the creep strainε(t) of a material under a stress σ(t) variable over time(1)εt=σ0ψt+∫0tσ˙τψt-τdτ,where ψ(t) is the creep function and σ0=σ(0) the stress applied at t=0. Note that the creep function ψ(t) coincides with the axial strain produced by the constant stress σ(t)=1. Integrating by parts (1) it follows(2)εt=σtψ0-∫0tστψ˙t-τdτ.By following [34], we write (2) in the form(3)εt=1E0σt-λ∫0tRαβ-λ,t-τστdτ,where(4)Rαβ-λ,t-τ=t-τα∑n=0∞β-λnt-τn1+αΓn+11+α,ψ0=1E0,λ=E0-E∞E0β,where Rα is the Rabotnov function that allows using fraction-exponential kernel in viscoelastic operators, and E0, E∞ are the elastic Young modulus at t=0, t→∞, respectively. A constant stress σ(t)=σ0 is then assumed in order to simulate the creep test, so that(5)∫0tRαβ-λ,t-τστdτ=σ0∑n=0∞β-λnΓn+11+α∫0tt-τn1+α+αdτ=σ0∑n=0∞β-λnt-τn+11+αΓn+11+α+1,where the property of Euler gamma function Γ(z+1)=zΓ(z) has been used.By shifting the indexm=n+1, it follows(6)σ0β-λ∑n=0∞β-λn+1tn+11+αΓn+11+α+1=σ0β-λ∑m=0∞β-λmtm1+αΓm1+α+1-1=σ0β-λM1+αβ-λt1+α-1,where the Mittag-Leffler function,(7)Maz=∑m=0∞zmΓma+1,has been introduced. Therefore, (3) becomes(8)εt=σ0E01-λβ-λM1+αβ-λt1+α-1.By using the following properties of the Mittag-Leffler function(9)limt→0⁡M1+αβ-λt1+α=1,limt→∞⁡M1+αβ-λt1+α=0,then, from (8) and (9), it follows(10)ε0=limt→0⁡εt=σ0E0,ε∞=limt→∞⁡εt=σ0E∞,where ε0 and ε∞ are the creep strains at t=0, t→∞, respectively.Again, let us consider the Boltzmann convolution integral that describes the relaxation stressσ(t) of a material under a strain variable over time ε(t).(11)σt=ε0ϕt+∫0tε˙τϕt-τdτ,where ϕ(t) is the relaxation function and ε0=ε(0) the strain applied at t=0. The relaxation function ϕ(t) coincides with the axial stress produced by the constant strain ε(t)=1. Integrating by parts (11) it follows(12)σt=εtϕ0-∫0tετϕ˙t-τdτ.By following [34], (12) can be written in the form(13)σt=E0εt+λ∫0tRαβ,t-τετdτ,ϕ0=E0.Assuming a constant strain ε(t)=ε0 in order to simulate the stress relaxation test and following the way to find (8), (13) becomes(14)σt=E0ε01+E0-E∞E0M1+αβt1+α-1.For the properties of the Mittag-Leffler function, from (14) it follows (15)σ0=limt→0⁡σt=E0ε0,σ∞=limt→∞⁡σt=E∞ε0,where σ0 and σ∞ are the stress relaxation at t=0, t→∞, respectively.The equations (8) and (14) represent the model by means of the fact that it was possible to fit accurately the experimental creep and stress relaxation tests for suitable values of parameters α and β. The plots of experimental and analytical creep and stress relaxation curves are reported in Figure 2(a) and the corresponding parameters α and β are reported in Table 2.Table 2
Parametersα and β that fit experimental creep and relaxation curves using the model given by (8) and (14).
α (dimensionless) - 1 / 3 β   ( s - ( 1 + α ) ) - 1 / ( 100 3 )Figure 2
(a) Experimental creep curve (dashed orange curve) and analytical creep curve according to (8) (solid red curve). Experimental stress relaxation curve (dashed cyan curve) and analytical stress relaxation curve according to (14) (dashed blue curve) both scaled by 1/2000. (b) Relative error between experimental data on creep and relaxation and their model given by (8) and (14).
(a) (b)Figure 3
Polypropylene fibres used for tensile until breakage and creep and stress relaxation tests [3].


## 3.1. Analytical Model for Creep and Stress Relaxation Curves

We wanted to fit experimental creep and stress relaxation curves with an analytical model by using fraction-exponential kernel that on one side fits carefully experimental data and, at the same time, allows analytical expression for inverse Laplace transform. Let us consider the Boltzmann convolution integral that describes the creep strainε(t) of a material under a stress σ(t) variable over time(1)εt=σ0ψt+∫0tσ˙τψt-τdτ,where ψ(t) is the creep function and σ0=σ(0) the stress applied at t=0. Note that the creep function ψ(t) coincides with the axial strain produced by the constant stress σ(t)=1. Integrating by parts (1) it follows(2)εt=σtψ0-∫0tστψ˙t-τdτ.By following [34], we write (2) in the form(3)εt=1E0σt-λ∫0tRαβ-λ,t-τστdτ,where(4)Rαβ-λ,t-τ=t-τα∑n=0∞β-λnt-τn1+αΓn+11+α,ψ0=1E0,λ=E0-E∞E0β,where Rα is the Rabotnov function that allows using fraction-exponential kernel in viscoelastic operators, and E0, E∞ are the elastic Young modulus at t=0, t→∞, respectively. A constant stress σ(t)=σ0 is then assumed in order to simulate the creep test, so that(5)∫0tRαβ-λ,t-τστdτ=σ0∑n=0∞β-λnΓn+11+α∫0tt-τn1+α+αdτ=σ0∑n=0∞β-λnt-τn+11+αΓn+11+α+1,where the property of Euler gamma function Γ(z+1)=zΓ(z) has been used.By shifting the indexm=n+1, it follows(6)σ0β-λ∑n=0∞β-λn+1tn+11+αΓn+11+α+1=σ0β-λ∑m=0∞β-λmtm1+αΓm1+α+1-1=σ0β-λM1+αβ-λt1+α-1,where the Mittag-Leffler function,(7)Maz=∑m=0∞zmΓma+1,has been introduced. Therefore, (3) becomes(8)εt=σ0E01-λβ-λM1+αβ-λt1+α-1.By using the following properties of the Mittag-Leffler function(9)limt→0⁡M1+αβ-λt1+α=1,limt→∞⁡M1+αβ-λt1+α=0,then, from (8) and (9), it follows(10)ε0=limt→0⁡εt=σ0E0,ε∞=limt→∞⁡εt=σ0E∞,where ε0 and ε∞ are the creep strains at t=0, t→∞, respectively.Again, let us consider the Boltzmann convolution integral that describes the relaxation stressσ(t) of a material under a strain variable over time ε(t).(11)σt=ε0ϕt+∫0tε˙τϕt-τdτ,where ϕ(t) is the relaxation function and ε0=ε(0) the strain applied at t=0. The relaxation function ϕ(t) coincides with the axial stress produced by the constant strain ε(t)=1. Integrating by parts (11) it follows(12)σt=εtϕ0-∫0tετϕ˙t-τdτ.By following [34], (12) can be written in the form(13)σt=E0εt+λ∫0tRαβ,t-τετdτ,ϕ0=E0.Assuming a constant strain ε(t)=ε0 in order to simulate the stress relaxation test and following the way to find (8), (13) becomes(14)σt=E0ε01+E0-E∞E0M1+αβt1+α-1.For the properties of the Mittag-Leffler function, from (14) it follows (15)σ0=limt→0⁡σt=E0ε0,σ∞=limt→∞⁡σt=E∞ε0,where σ0 and σ∞ are the stress relaxation at t=0, t→∞, respectively.The equations (8) and (14) represent the model by means of the fact that it was possible to fit accurately the experimental creep and stress relaxation tests for suitable values of parameters α and β. The plots of experimental and analytical creep and stress relaxation curves are reported in Figure 2(a) and the corresponding parameters α and β are reported in Table 2.Table 2
Parametersα and β that fit experimental creep and relaxation curves using the model given by (8) and (14).
α (dimensionless) - 1 / 3 β   ( s - ( 1 + α ) ) - 1 / ( 100 3 )Figure 2
(a) Experimental creep curve (dashed orange curve) and analytical creep curve according to (8) (solid red curve). Experimental stress relaxation curve (dashed cyan curve) and analytical stress relaxation curve according to (14) (dashed blue curve) both scaled by 1/2000. (b) Relative error between experimental data on creep and relaxation and their model given by (8) and (14).
(a) (b)Figure 3
Polypropylene fibres used for tensile until breakage and creep and stress relaxation tests [3].


## 4. Conclusions

In the present paper we carried out a tensile test until breakage and a creep and stress relaxation test on a PP fibre and fitted these experimental tests by using a viscoelastic model based on fractional-exponential kernel. The curves plotted in Figure2(a) show that the theoretical model closely fits the experimental results. The relative error, showing the deviation between the experimental data and the theoretical prediction, is plotted in Figure 2(b). It shows a maximum relative error of 5% and 10%, respectively, for creep and relaxation, occurring in a very small portion of the curves.Conversely to complex viscoelastic models based on combinations of Maxwell and Kelvin-Voight schemes, the proposed model requires the calibration of only two parameters (α and β) to simulate creep and relaxation phenomena [35]. Moreover, for simple load or displacement histories, it allows calculating straightforwardly the stress and strain fields based on the calculation of the inverse Laplace transform in closed form. Note also that the Rabotnov function generally allows fitting the experimental data better than other conventional schemes based on the combination of springs and dashpots [34].It has been proved that the model here adopted is able to match carefully experimental data obtained for PP fibres. In a forthcoming work, the present investigation will be extended in order to take into account the effects induced by thermal variations acting on FRC elements (for the thermodynamic aspects of thermoelasticity, see, e.g., [44]).



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*Source: 3823047-2016-11-27.xml*