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WO1999008033A1 - Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide - Google Patents

Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide Download PDF

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Publication number
WO1999008033A1
WO1999008033A1 PCT/US1997/013342 US9713342W WO9908033A1 WO 1999008033 A1 WO1999008033 A1 WO 1999008033A1 US 9713342 W US9713342 W US 9713342W WO 9908033 A1 WO9908033 A1 WO 9908033A1
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WO
WIPO (PCT)
Prior art keywords
strength
ribbon
pipe
weeping
reinforcement
Prior art date
Application number
PCT/US1997/013342
Other languages
English (en)
Inventor
Liza Monette
Allen S. Chiu
Russell R. Mueller
Michael P. Anderson
Original Assignee
Exxon Research And Engineering Company
Priority date (The priority date is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the date listed.)
Filing date
Publication date
Priority to CA2194788A priority Critical patent/CA2194788A1/fr
Priority to NO970390A priority patent/NO970390D0/no
Priority to JP9032975A priority patent/JPH09207235A/ja
Application filed by Exxon Research And Engineering Company filed Critical Exxon Research And Engineering Company
Priority to CA002296074A priority patent/CA2296074A1/fr
Priority to AU37424/97A priority patent/AU3742497A/en
Priority to EP97934345A priority patent/EP1015801A4/fr
Priority to PCT/US1997/013342 priority patent/WO1999008033A1/fr
Priority to JP2000506476A priority patent/JP2001512814A/ja
Publication of WO1999008033A1 publication Critical patent/WO1999008033A1/fr
Priority to NO20000332A priority patent/NO20000332L/no

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Classifications

    • F—MECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F16—ENGINEERING ELEMENTS AND UNITS; GENERAL MEASURES FOR PRODUCING AND MAINTAINING EFFECTIVE FUNCTIONING OF MACHINES OR INSTALLATIONS; THERMAL INSULATION IN GENERAL
    • F16L—PIPES; JOINTS OR FITTINGS FOR PIPES; SUPPORTS FOR PIPES, CABLES OR PROTECTIVE TUBING; MEANS FOR THERMAL INSULATION IN GENERAL
    • F16L9/00—Rigid pipes
    • F16L9/12—Rigid pipes of plastics with or without reinforcement

Definitions

  • This invention relates to polymer-glass ribbon composite laminates for fluid containment.
  • this invention relates to a modification to the reinforcement morphology of polymer-glass fiber composite laminates designed to increase the strength and longevity of pressure containing devices made from such laminates (under static pressure) and fatigue performance (under cyclic pressure).
  • Pressure containing devices include: pipes, downhole tubulars, pipelines, pressure vessels, underground storage tanks. Other applications include composite wraps and crack arrestors. Containment pressure can be increased from current commercially available levels up to 5000 psig long term service pressure.
  • the performance of pressure containing devices is limited by poor mechanical properties of the individual laminates, in the direction normal to the fiber axis. It has been found that the use of glass ribbons having aspect ratio between 10 and 1000 in the direction normal to the ribbon axis (e.g. ribbon or tape morphology) as reinforcement results in increases to normal stiffness and strength of the composite laminate providing an enhancement in containment capability.
  • Pressure containing devices such as pipes, downhole tubulars, underground storage tanks, pressure vessels, pipelines, wraps and crack arrestors
  • fabricated from epoxy-fiber glass composites are increasingly used in oil and gas production.
  • low pressure piping in entire fields are being upgraded to take advantage of these materials.
  • the benefits of composites over equivalent metal structures primarily involve their superb corrosion resistance, leading to a decreased life- cycle cost.
  • Other attractive advantages include their high strength and stiffness per unit weight, flexibility in material design, and improved fatigue resistance.
  • polymer composites as presently supplied contain a serious deficiency that precludes their use in applications that generate even moderate stress levels.
  • the composite material exhibits an axial strength (in the fiber direction) of up to 200 ksi (with pristine glass fibers), 100 ksi (for non-pristine glass fibers) the device exhibits a loss of fluid containment integrity referred to as weeping, by which matrix microcracking and ply delamination provide a leak path for the fluid at short and long term service pressures which are an order of magnitude less than the burst pressure.
  • the microcracking can be alleviated by increasing the pipe wall thickness.
  • this solution drives the composite pipe cost up by approximately 30% as compared to that of carbon steels (for example, a 2000 psi pressure, 2-7/8" outside diameter downhole tubing). This higher cost constitutes a barrier to the substitution of composite pipes for carbon steels in low pressure applications (i.e. flow lines).
  • Composite pipes have not as yet been introduced in more demanding, higher pressure functions (pipelines), as the cost of increasing further the wall thickness becomes prohibitive.
  • composites used as downhole tubulars do not compete favorably against the more expensive corrosion resistant alloys (CRAs).
  • CRAs corrosion resistant alloys
  • the required wall thickness of composite tubulars prevents their use in many applications where the diameter of the hole connecting the oil in geologic formation to the surface is constrained.
  • Other devices such as composite underground storage tanks also exhibit premature microcracking, hence their corrosion resistance does not offer any additional advantages over similar metal structures. Matrix microcracking occurring in composite wraps considerably reduces their longevity (for construction/rejuvenation applications), as moisture eventually diffuses through the resulting cracks and directly attacks the glass, thereby weakening the reinforcement.
  • the polymer matrix in these composite pipes is typically a thermosetting system, e.g. an epoxy, which solidifies by cross-linking (chemical reaction).
  • Thermoplastic systems can also be envisioned as an acceptable material.
  • the matrix in this case solidifies by a physical phenomenon such as crystallization from the melt.
  • the cross-linked thermosetting plastic has a Young's modulus around 430 ksi, and a tensile strength between 11-13 ksi and a tensile elongation to failure less than 25%.
  • Continuous glass reinforcement (currently fibers with a diameter 15 ⁇ m, volume fraction 60%) are embedded in a mixture of thermosetting resin and curing agent.
  • the mixture is initially uncured, so its viscosity is usually low enough (few hundreds cp) to ensure reasonable wetting of the glass reinforcement by the mixture.
  • the resulting ply is wound around a mandrel, at an angle between 0° and 90° with respect to the pipe axis.
  • the winding angle ⁇ is 55°, and the laminate is viewed in a direction along the fiber length or axis.
  • the winding angle ⁇ is then tilted to 125° (or -55°) upon reaching the end of the mandrel, then back to 55° and so on.
  • Several winding angles can be used in this process, i.e. 0, ⁇ 45° and ⁇ 70°.
  • the resulting pipe is referred to as a multidirectional filament wound pipe.
  • the pipe is subsequently heat treated, so the thermosetting resin can solidify by cross-linking.
  • the result is a pipe, referred to as filament wound pipe, with inside diameter typically ranging from 1" to 36" and wall thickness from 0.1" to 2.0".
  • Common pipe dimensions consists of 4" inside diameter and 0.16" wall thickness.
  • Figure 2 shows a short-term failure envelope, i.e. fluid containment limits due to matrix micro-cracking, weeping, measured for a representative composite pipe with fiber/matrix parameters and dimensions as described in the paragraph above, under different petrochemical service conditions: 1. Pure axial stress; 2. Hoop stress equal to axial stress (downhole tubulars); 3. Hoop stress twice the axial stress (surface pipes); and 4. Pure hoop stress (buried pipes).
  • the service pressure can be obtained by dividing the value of the hoop strength on the graph by the ratio R/T (inside radius over the wall thickness) and by a service factor of 4 to account for visco-elastic relaxation of matrix (static pressure), or matrix fatigue behavior (cyclic pressure) for long-term service (20 years).
  • such a pipe used as a downhole tubular can withstand a service pressure of 500 psig; used as a surface pipe, a service pressure of 1500 psig; and used as a buried pipe, a service pressure of 1000 psig.
  • the present invention is a high weeping strength polymer-glass ribbon composite laminate for fluid containment.
  • the laminate includes a reinforced composite tubular body which comprises a tubular polymeric matrix including a thermosetting polymer with tensile elongation to break less than 25% and a glass reinforcing strip or ribbon embedded within said tubular polymeric matrix.
  • the reinforcing strip may be helically wound about the longitudinal axis of said tubular body or wound at an angle between -90° and 90° with respect to the pipe axis.
  • the axial Young's modulus of the tubular body is greater than 50% of the rule of mixture value.
  • Figure 1 shows an example of a reinforced tube with the winding at an angle of 55°.
  • the fiber volume fraction is 60%.
  • the reinforcement illustrated consists of conventional glass fibers.
  • Figure 2 shows a failure envelope with containment limits for matrix micro-cracking and weeping.
  • Figure 3 shows the stresses induced by gas or fluid pressure in the wall of a typical epoxy-based pipe.
  • the winding angle is 55°.
  • FIG. 4 shows the relationships in the coarse-grained spring model used in the present invention.
  • kj is the spring constant between two nearest neighbors
  • k is the spring constant between two next-nearest neighbors
  • Figure 5 shows the stress-strain plot according to the simulation model applied to a typical laminate with conventional glass fibers having a volume fraction of 58%.
  • the strain ⁇ is applied in the direction normal to the fiber axis, according to the simulation model.
  • Figure 6a shows a schematic of a metal ribbon/epoxy pipe.
  • Figure 6b shows a cross-section of the pipe wall of Figure 6a.
  • Aspect ratios s ⁇ s c are not desirable because of poor load transfer properties.
  • Aspect ratios s > 5s c may compromise the ease of processing, even though load transfer is close to ideal.
  • Figures 10a and 10b show a glass ribbon composite pipe and wall cross- section for a random distribution of reinforcement.
  • Figure 1 la shows a short-term failure envelope of invention, a glass ribbon/epoxy pipe (full circles, dashed line), as compared to failure envelope of current ⁇ 55° glass fiber/epoxy pipe (full squares, full line).
  • Figure 1 lb shows a long-term failure envelope of invention, a glass ribbon/epoxy pipe (full circles, dashed line), as compared to failure envelope of current ⁇ 55° glass fiber/epoxy pipe (full squares, full line).
  • Figure 12a shows a short-term failure envelope of invention, a glass ribbon/epoxy pipe (full circles, dashed line), as compared to failure envelope of current ⁇ 55° glass fiber/epoxy pipe (full squares, full line).
  • Figure 12b shows a long-term failure envelope of invention, a glass ribbon/epoxy pipe (full circles, dashed line), as compared to failure envelope of current ⁇ 55° glass fiber/epoxy pipe (full squares, full line).
  • Random Ribbon Reinforcement Distribution a. Critical Aspect Ratio For Random Ribbon Distribution b. Transverse Laminate Tensile Weeping Strength c. Selection Criteria/Range of Values
  • ⁇ L ⁇ ⁇ sin 2 ⁇ + ⁇ z cos 2 ⁇ (4)
  • ⁇ N ⁇ ⁇ cos 2 ⁇ + ⁇ z sin 2 ⁇ (5)
  • ⁇ L is comparable to ⁇ N , for service conditions 2, 3 and 4 on fig. 2.
  • the strength in the direction along the reinforcement axis (L) is controlled by the reinforcement strength, and is approximately 60 ksi.
  • the strength in the direction normal to the reinforcement axis (N) is controlled by the matrix strength in the case of conventional fibers.
  • the resulting laminate short-term normal strength will be shown below to be less than 10 ksi for conventional fibers.
  • the axial failure stress on fig. 2 can be related to the normal laminate strength by a simple analysis using eq. (5) and setting ⁇ ⁇ to 0:
  • the normal laminate strength ⁇ N may be deduced from eq. (7), using the empirical axial failure stress of 11.25 ksi for conventional fiber-composites (point 1 on fig. 2), and its value is 7.5 ksi for 60% fiber content. This value will be used later for computer model validation.
  • a model methodology is introduced here and will be used to demonstrate the concept on which the invention is based:
  • a ribbon-like reinforcement morphology increases the amount of load transfer, hence the ply strength in the direction normal to the reinforcement axis.
  • the elastic properties of the simulation model have been described elsewhere (L. Monette, M. P. Anderson, H. D. Wagner and R. R. Mueller, J. Appl. Phys. 76 (1994) 1442) (L. Monette and M. P. Anderson, Modelling Simul. Mater. Eng. 2 (1994) 53), and will be briefly mentioned here.
  • the simulation model is a coarsegrained spring model on a two dimensional lattice of dimensions 200 x 200, with spring constants k ⁇ p and bond bending constants c ⁇ .
  • ⁇ ik, im, io and iq on fig.4).
  • ⁇ dioxide is the angle between bonds ⁇ and ⁇ , and the equilibrium angles
  • c ⁇ p c m if bonds ⁇ and ⁇ are matrix bonds.
  • c ⁇ p c if bonds ⁇ and ⁇ are glass bonds.
  • c ⁇ p c ⁇ , if bonds ⁇ and ⁇ are a matrix and glass bonds, or a glass and matrix bonds, respectively.
  • the energy Vj; stored in a bond between nodes i and j is:
  • V ⁇ K k i j ( r ⁇ - r ii°) 2+1/2 ⁇ C ⁇ ( COs ⁇ ⁇ P ⁇ -COs ⁇ 0 ) 2 (11)
  • Periodic boundary conditions are used in the direction of applied tensile strain or stress, while free boundary conditions are applied in the other direction. Mechanical equilibrium of the system is ensured by a conjugate gradient technique.
  • the present simulation model incorporates a failure criterion via the cohesive energy parameter Ujj.
  • the tensile elongation of the matrix at break is less than 0.25, for example,
  • Tensile elongation is defined as change in length over original length, — .
  • the model is subsequently used to simulate the stiffness and strength of a conventional glass fiber laminate, in the direction normal to the fiber axis.
  • the poor loading of the reinforcement in the direction normal to the fiber axis implies that the laminate strength in that direction is matrix-dominated, as the matrix always exceeds its tensile failure criterion first.
  • the fibers can be viewed in that direction as two dimensional particles which do not carry a load significantly greater than that of the matrix. Furthermore, when close enough to one another, they act as stress raisers, causing stress amplifications in the matrix material. Therefore, the occurrence of failure is expected at a value of external applied stress much less than the strength value of the pure matrix material.
  • the normal laminate strength is usually less than the strength of the pure matrix materials, hence the empirical value of 7.5 ksi deduced in 1. above for a 60% reinforcement volume fraction is less than the strength 13 ksi for the pure matrix material.
  • Figure 5 is a stress/strain curve obtained from the model for a conventional laminate with a fiber volume fraction of 58%, typical of the laminates used for pipe fabrication.
  • the normal laminate strength is 8 ksi, a value within 7% of the empirical value of 7.5 ksi. It is therefore concluded that the model yields conventional glass fiber laminate normal strength in good agreement with that of a real conventional glass fiber laminate.
  • Strip (or ribbon) reinforced composites are known in the art see US patent 3,790,438, to provide enhanced mechanical properties, but are limited to polymers with a tensile elongation greater than 25%. The reason given for this strain limitation is that the matrix material must have sufficient elongation to decrease the effect of stress concentrations due to thermal stresses arising during the manufacturing process.
  • Metal strip reinforced tubular body in which the matrix (typically a thermoset) has a tensile elongation less than 25% have recently been proposed see US patent 4,657,049.
  • the invention is described as providing a tubular body comprised of a thermosetting polymer in which metallic reinforcing strips are completely embedded such that the entire load borne by the polymer is distributed to the reinforcing strips.
  • the advantages of the invention are claimed to be such that it:
  • US patent 3,790,438 limits the range of validity of their invention (strip reinforced composites) to polymeric matrices with tensile elongation equal or greater than 25%.
  • the polymeric material typically used in composite pipes for oil/gas applications is a thermoset, which has a tensile elongation less than 25%. Therefore, US patent 3,790,438 does not teach how to improve mechanical properties of composites where the matrix has a tensile elongation less than 25%.
  • O R is the tensile strength of the reinforcement
  • ⁇ is the shear strength of the interface between the reinforcement and the polymeric matrix
  • t is the strip thickness.
  • the tensile weeping resistance ⁇ w of US patent 4,657,049 metal strip reinforced tubular, as measured by the simulation model described in section 2 is 3 to 4 times less than the predicted pipe axial strength ⁇ . Therefore, the pipe tensile weeping strength ⁇ w , which is the pipe usable strength before occurrence of loss of containment, is a property independent of the pipe ideal axial strength ⁇ .
  • the tensile stress level ⁇ a at which matrix microcracking first appears as determined by the simulation model for the US patent 4,657,049 metal strip reinforced tubular is 0.5 to 0.8 lower than the tensile weeping strength of conventional +55° filament wound fiberglass/epoxy pipes. This implies that US patent 4,657,049 metal strip reinforced tubular is likely to loose its corrosion resistance at service pressures where state of the art composite pipes/tubulars provide corrosion resistance.
  • the initial matrix microcracking encountered at these lower tensile strengths provides an entry path for the corrosive fluids present in petrochemical applications to attack and progressively degrade the metal reinforcement.
  • the principle on which the present invention is based is that the load transfer in the direction normal to the reinforcement axis must be increased, in order to increase the laminate transverse strength, hence the composite resistance to weeping.
  • An approach to increase load transfer is to modify the reinforcement morphology, i.e. from cylindrical to ribbon-like, as to increase the surface area in the transverse direction. This increased surface area is expected to give rise to shear tractions, which lead to increased reinforcement loading in the laminate transverse direction.
  • the reinforcement has a ribbon-like cross-section made of bulk glass, such that it possesses a normal aspect ratio (ratio of ribbon width over thickness) much greater than one.
  • the required ribbon width is 2.5 mm.
  • a stress field analysis indicates that the load transfer in the normal direction from the matrix to the reinforcement has been greatly improved.
  • the average stress transferred to the reinforcement in the direction along the ribbon width can be three times higher than that transferred to the same volume fraction of reinforcement with cylindrical morphology, i.e. fibers (see Section II).
  • the average stress carried by the matrix is consequently three times less than that carried by the matrix for a cylindrical reinforcement (see Section II).
  • the load transfer from the matrix to the reinforcement now occurs by a shear-lag mechanism (H. L. Cox, Br. J. Appl. Phys. 3 (1952) 72), i.e. by shear tractions along the ribbon width at the reinforcement/matrix interface. Therefore, both the laminate Young's modulus and strength in the direction normal to the fiber axis are expected to increase significantly above the matrix value.
  • the composite parameters which may influence the laminate transverse strength are: E (reinforcement Young's modulus), E m (matrix Young's modulus), ratio s/s c (where s is the ribbon transverse aspect ratio and s c the ribbon transverse critical aspect ratio), ⁇ j (interface shear strength), ⁇ m (matrix tensile strength) and V f (the reinforcement volume fraction).
  • E force Young's modulus
  • E m matrix Young's modulus
  • ratio s/s c where s is the ribbon transverse aspect ratio and s c the ribbon transverse critical aspect ratio
  • ⁇ j interface shear strength
  • ⁇ m matrix tensile strength
  • V f the reinforcement volume fraction
  • E N Vf(E R -Em)( ⁇ R )N/( ⁇ a)N + E m (16)
  • E N tends asymptotically to the rule of mixture value
  • E RM V f (E R - E m ) + E m as the ribbon transverse aspect ratio s — ⁇ .
  • the rule of mixtures defines the maximum property level (here ERM) a multi-component structure can possess, based on the property level of the individual components (E R , E m ), averaged on the basis of their respective volume fraction, or concentration.
  • ERM maximum property level
  • the three most important composite parameters for this invention are: 1) s c , the transverse ribbon critical aspect ratio
  • ⁇ is a function which depends on the ribbon distribution, and will be further described in the section 4.3.
  • s is the ribbon transverse aspect ratio, and should be selected once s c is known, such that the transverse ribbon laminate modulus in eq. (18) can be optimized, i.e. to be increased as close to ideal limit.
  • E R , E m , Vf and s/s c are set, the important composite parameters to maximize the transverse failure strain are obtained from eq. (15), i.e. 2) the interfacial shear strength x t and 3) matrix tensile strength ⁇ m . Range of values for both will also be given in section 4.3.
  • V f 50%
  • the matrix is an epoxy, typically used for filament wound pipes for petrochemical applications, with the following properties:
  • the interfacial shear strength for a glass/epoxy system has been estimated from fragmentation experiments.
  • the tensile weeping strength of the present invention is 2.3 times greater than the tensile weeping strength of the US patent 4,657,049 invention, both determined by the simulation model.
  • s c ⁇ 160 for the metal ribbon and s c ⁇ 40 for the glass ribbon are therefore greater for glass than metal ribbons, where the ribbon aspect ratios selected (i.e. 160 and 400) are only 1 to 2 times greater that the critical aspect ratio for the metal ribbon reinforcement, while the same ribbon aspect ratio is 4 to 10 times greater than the critical aspect ratio when the ribbon is made out of bulk glass .
  • the greater load transfer efficiency, together with increased interfacial shear strength and matrix strength explains the greater tensile weeping strength of the current invention, as compared to US patent 4,657,049 invention.
  • figs. 9a and 9b illustrates a ribbon composite pipe and wall cross section which has a ribbon distribution with £ ⁇ 0.1L (i.e. as small as possible), and L 0 ⁇ L/2. Note that the lowest volume fraction v "" 1 achievable with distribution (21a) (see fig. 8b) or distribution (21b) (fig. 9b) is
  • Tables 3, 4 and 5 make use of same matrixinterface parameters as for table 2.
  • Tables 7, 8 and 9 make use of same matrix interface parameters as for table 2.
  • the only way to increase the composite transverse laminate weeping strength is either to increase the interfacial shear strength, or choose a system with a high interfacial shear strength such as glass/epoxy system.
  • Glass ribbons with aspect ratio s > 2s c will impart to the invention an axial weeping strength superior to the state of the art composite pipes made with conventional glass fibers.
  • the invention axial weeping strength is 4.5 times stronger than currently available ⁇ 55° filament wound pipes, and 2.4 times stronger than currently available multidirectional filament wound pipes. d. Selection Criteria/Ranges of values
  • the critical ribbon transverse aspect ratio can be determined by eq. (24) for lay-ups with 0.1L ⁇ £ ⁇ L/2; and by eq. (25) for lay-ups with £ ⁇ 0.1L. Comparing Equation (23) yields the average tensile strain transferred to the reinforcement, and normalized to the
  • Reinforcement volume fraction should be in the range 0.4 ⁇ V f ⁇ 0.8, preferably in the range 0.5 ⁇ Vf ⁇ 0.7.
  • the average tensile strain transferred to the reinforcement should be at least greater than 50% of the applied strain with preferred value around 80%. Therefore this requires a ribbon transverse aspect ratio s > 4.5 s c for lay-ups with 0.02L ⁇ £ ⁇ L/2, while s > 3s c for lay-ups with £ ⁇ 0.02L.
  • the modulus ratio ER/E ⁇ could assume any value, but the higher its value, the higher is the interfacial shear strength needed to ensure increased laminate transverse strength.
  • E R /E m For ER/ ⁇ m > 50, we recommend an interfacial shear strength around 6 ksi, or greater.
  • the matrix tensile strength should not be below the value for the interfacial shear strength, i.e. ⁇ m > x,
  • Figure 10 illustrate the present invention, a ribbon laminate wound pipe with winding angle between 0 and 90° with respect to pipe axis.
  • the next layer of laminate is wound at an angle opposite in magnitude (sign) to the pipe axis in the preceding layer, although not necessarily the exact opposite degree of winding angle.
  • the winding angle is +90°, as an example.
  • the laminate shear stress vanishes.
  • Figure 10b is a cross-sectional view of a laminate made of a random arrangement of ribbon-like reinforcement. This distribution would be appropriate for ribbon-like reinforcement which is very thin, t ⁇ 0.05mm and narrow.
  • the laminate thickness should not be less than 0.1mm, so the manufacturing costs of the invention do not increase.
  • the reinforcement /matrix /interface parameters are the same as the ones used for table 2.
  • Glass ribbons with aspect ratio 4 times or more the critical aspect ratio will impart to the invention an axial weeping strength superior to the state of the art composite pipes.
  • the critical ribbon transverse aspect ratio can be determined by eqs (26) and (27).
  • the ribbon aspect ratio should be at least 4 to 5 times greater than the critical aspect ratio.
  • the modulus ratio E R /E m could assume any value, but the higher its value, the higher the interfacial shear strength is needed to ensure increased laminate transverse strength. We feel a range 20 ⁇ E R /E m ⁇ 100 is reasonable, with the load transfer efficiency being optimum for E R /E m closer to the lower limit.
  • Reinforcement volume fraction should be in the range 0.4 ⁇ V f ⁇ 0.8, preferably in the range 0.5 ⁇ Vf ⁇ 0.7.
  • E R /E m > 50 we recommend an interfacial shear strength around 6 ksi, or greater.
  • the matrix tensile strength should not be below the value for the interfacial shear strength, i.e. ⁇ m > ⁇
  • the failure criterion used here is based on the von Mises failure criterion (D. Hull, "An Introduction to Composite Materials", Cambridge University press, (1981) p. 169) which was originally applied to homogeneous and isotropic bodies, then expanded and modified by Hill to anisotropic bodies, and applied to composite materials by Tsai:
  • the long term performance of the invention is expected to be much better than current composite pipe.
  • the long term weeping strength of current pipe is compared with expected long term weeping strength of the invention in fig. 1 lb.
  • the improvement in long term performance of the invention versus state of the art composite pipe is a factor of 12 in the axial weeping strength (point 1 on fig. 1 lb); a factor of 4 for both downhole tubing and buried pipe applications (points 2 and 4 on fig. 1 lb); and a factor of 2 for surface pipe application (point 3) on fig. 1 lb.
  • the fiber, interface and matrix have same mechanical properties as for section A.
  • ⁇ L 100 ksi, ⁇ N ⁇ 34 ksi (see Table 16).
  • the failure criterion is same as for section A.
  • the short term weeping strength for the downhole tubing application (i.e. point 2), as well as for buried pipe application (point 4) are increased by a factor of 0.33 and 2 respectively.
  • the short term weeping strength of the surface pipe application (point 3) is decreased by 20%.
  • the long term weeping strength of current pipe is compared with expected long term weeping strength of the invention in fig. 12b.
  • the new service factor is calculated as in section A and is 0.5.
  • the improvement in long term performance of the invention versus state of the art composite pipe is a factor of 6 in axial weeping strength; a factor of 2.5 for downhole tubing application (point 2 on fig. 12b); a factor of 4 for buried pipe application (point 4); and a factor of 1.5 for surface pipe application (point 3)
  • the glass ribbons described in this patent can be fabricated in several ways.
  • One approach which is used commercially is the utilization of a redraw process, where an oversize preform with desired section geometry is heated to its softening point and then pulled, see US patent 3,425,454, Feb. 4, 1969.

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  • Engineering & Computer Science (AREA)
  • General Engineering & Computer Science (AREA)
  • Mechanical Engineering (AREA)
  • Moulding By Coating Moulds (AREA)
  • Laminated Bodies (AREA)
  • Reinforced Plastic Materials (AREA)
  • Rigid Pipes And Flexible Pipes (AREA)

Abstract

La présente invention concerne un stratifié composite à ruban de verre polymère à résistance au suintement élevée pour réservoirs de fluide. Ce stratifié est constitué d'un corps tubulaire composite renforcé, qui renferme une matrice polymère tubulaire comprenant un polymère thermodurcissable, l'allongement à la rupture sous tension de cette matrice étant inférieur à 25 %, et un renfort de ruban de verre, encapsulé dans cette matrice polymère tubulaire. Ce ruban de renforcement peut être enroulé de manière hélicoïdale selon un angle variant entre 0 et 90 % par rapport à l'axe du tuyau, ou enroulé selon un angle d'environ 90° par rapport à cet axe.
PCT/US1997/013342 1996-01-30 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide WO1999008033A1 (fr)

Priority Applications (9)

Application Number Priority Date Filing Date Title
CA2194788A CA2194788A1 (fr) 1996-01-30 1997-01-09 Composite polymère-fibre de verre à haute résistance au suintement pour retenue de liquides
NO970390A NO970390D0 (no) 1996-01-30 1997-01-29 Polymer-glassfiber komposittlaminater
JP9032975A JPH09207235A (ja) 1996-01-30 1997-01-30 流体格納用の高ウィーピング強度ポリマー−ガラス繊維複合積層体
CA002296074A CA2296074A1 (fr) 1997-07-22 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide
AU37424/97A AU3742497A (en) 1997-07-22 1997-07-22 High weeping strength polymer-glass ribbon composite laminates for fluid containment
EP97934345A EP1015801A4 (fr) 1996-01-30 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide
PCT/US1997/013342 WO1999008033A1 (fr) 1996-01-30 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide
JP2000506476A JP2001512814A (ja) 1997-07-22 1997-07-22 流体格納用の高ウィーピング強度ポリマー−ガラスリボン複合積層体
NO20000332A NO20000332L (no) 1997-07-22 2000-01-21 Sterkt lekkasjehindrende polymerglassbÕnd av komposittlaminater for fluidoppdemning

Applications Claiming Priority (2)

Application Number Priority Date Filing Date Title
US59407596A 1996-01-30 1996-01-30
PCT/US1997/013342 WO1999008033A1 (fr) 1996-01-30 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide

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PCT/US1997/013342 WO1999008033A1 (fr) 1996-01-30 1997-07-22 Stratifies composites a ruban de verre polymere a resistance au suintement elevee pour reservoirs de fluide

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EP (1) EP1015801A4 (fr)
JP (1) JPH09207235A (fr)
CA (1) CA2194788A1 (fr)
NO (1) NO970390D0 (fr)
WO (1) WO1999008033A1 (fr)

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WO2002088589A1 (fr) * 2001-04-27 2002-11-07 Solvay (Société Anonyme) Tube renforce en matiere plastique et procede de fabrication dudit tube
DE10238103C1 (de) * 2002-08-16 2003-09-18 Kanal Und Rohrtechnik Gmbh Verbundrohr und Verfahren zu seiner Herstellung
US7004202B2 (en) 2002-04-22 2006-02-28 Rib Loc Australia Pty Ltd. Composite strip windable to form a helical pipe and method therefor
US7721611B2 (en) 2003-11-07 2010-05-25 Conocophillips Company Composite riser with integrity monitoring apparatus and method
WO2015089267A1 (fr) * 2013-12-13 2015-06-18 Halliburton Energy Services, Inc. Outils renforcés par des fibres destinés à être utilisés en fond de trou
WO2016003464A1 (fr) * 2014-07-03 2016-01-07 Halliburton Energy Services, Inc. Outils renforcés de fibres continues pour un usage en fond de trou
US10145179B2 (en) 2013-12-13 2018-12-04 Halliburton Energy Services, Inc. Fiber-reinforced tools for downhole use
US11225843B2 (en) 2019-08-01 2022-01-18 Saudi Arabian Oil Company Composite dual channel drill pipes and method of manufacture

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ITTO20010782A1 (it) * 2001-08-03 2003-02-03 Campagnolo Srl Procedimento per la produzione di una pedivella per bicicletta.
AP2014008004A0 (en) * 2012-03-14 2014-10-31 Purapipe Holding Ltd Multilayer pipeline in a polymer material, device for manufacture of the multilayer pipeline and a method for manufacturing the multilayer pipeline

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NO337080B1 (no) * 2001-04-27 2016-01-18 Egeplast Werner Strumann Gmbh 6 Co Kg Forsterket plastrør og fremgangsmåte for fremstilling derav
BE1014145A3 (fr) * 2001-04-27 2003-05-06 Solvay Sociutu Anonyme Tube renforce en matiere plastique et procede de fabrication dudit tube.
US7093620B2 (en) 2001-04-27 2006-08-22 Solvay Reinforced plastic pipe and process for manufacturing the said pipe
KR100896226B1 (ko) * 2001-04-27 2009-05-08 에게플라스트 베르너 스트루만 게엠베하 운트 코. 카게 보강된 플라스틱 파이프와 이 파이프의 제조방법
WO2002088589A1 (fr) * 2001-04-27 2002-11-07 Solvay (Société Anonyme) Tube renforce en matiere plastique et procede de fabrication dudit tube
US7004202B2 (en) 2002-04-22 2006-02-28 Rib Loc Australia Pty Ltd. Composite strip windable to form a helical pipe and method therefor
US7174922B2 (en) 2002-04-22 2007-02-13 Rib Loc Australia Pty Ltd. Composite strip windable to form a helical pipe and method therefor
DE10238103C1 (de) * 2002-08-16 2003-09-18 Kanal Und Rohrtechnik Gmbh Verbundrohr und Verfahren zu seiner Herstellung
US7721611B2 (en) 2003-11-07 2010-05-25 Conocophillips Company Composite riser with integrity monitoring apparatus and method
CN105705724A (zh) * 2013-12-13 2016-06-22 哈里伯顿能源服务公司 井下使用的纤维增强工具
GB2547491A (en) * 2013-12-13 2017-08-23 Halliburton Energy Services Inc Fiber-reinforced tools for downhole use
WO2015088560A1 (fr) * 2013-12-13 2015-06-18 Halliburton Energy Services, Inc. Outils renforcés de fibres pour une utilisation en fond de trou
WO2015089267A1 (fr) * 2013-12-13 2015-06-18 Halliburton Energy Services, Inc. Outils renforcés par des fibres destinés à être utilisés en fond de trou
CN105705722A (zh) * 2013-12-13 2016-06-22 哈里伯顿能源服务公司 井下使用的纤维增强工具
GB2535370A (en) * 2013-12-13 2016-08-17 Halliburton Energy Services Inc Fiber-reinforced tools for downhole use
GB2535370B (en) * 2013-12-13 2020-05-27 Halliburton Energy Services Inc Fiber-reinforced tools for downhole use
US10156098B2 (en) 2013-12-13 2018-12-18 Halliburton Energy Services, Inc. Fiber-reinforced tools for downhole use
US10145179B2 (en) 2013-12-13 2018-12-04 Halliburton Energy Services, Inc. Fiber-reinforced tools for downhole use
US10060191B2 (en) 2014-07-03 2018-08-28 Halliburton Energy Services, Inc. Continuous fiber-reinforced tools for downhole use
GB2547499A (fr) * 2014-07-03 2017-08-23 Halliburton Energy Services Inc Outils renforces de fibres continues pour un usage en fond de trou
WO2016003464A1 (fr) * 2014-07-03 2016-01-07 Halliburton Energy Services, Inc. Outils renforcés de fibres continues pour un usage en fond de trou
CN106460466B (zh) * 2014-07-03 2019-01-15 哈利伯顿能源服务公司 用于井下使用的连续纤维增强工具
CN106460466A (zh) * 2014-07-03 2017-02-22 哈利伯顿能源服务公司 用于井下使用的连续纤维增强工具
US11225843B2 (en) 2019-08-01 2022-01-18 Saudi Arabian Oil Company Composite dual channel drill pipes and method of manufacture

Also Published As

Publication number Publication date
EP1015801A1 (fr) 2000-07-05
EP1015801A4 (fr) 2003-01-29
JPH09207235A (ja) 1997-08-12
NO970390D0 (no) 1997-01-29
CA2194788A1 (fr) 1997-07-31

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