Intermediate Temperature Heat Pipe Life Tests and Analyses

William G. Anderson1, Sanjida Tamanna2, Calin Tarau3, and John R. Hartenstine4
Advanced Cooling Technologies, Inc., Lancaster, PA, 17601, U.S.A.

David L. Ellis5
NASA Glenn Research Center, 21000 Brookpark Road, Cleveland, OH 44135 U.S.A.

43rd International Conference on Environmental Systems (ICES 2013), Vail, CO, July 14-18, 2013

There are a number of applications that could use heat pipes or loop heat pipes (LHPs) in the intermediate temperature range of 450 to 750 K, including space nuclear power system radiators, fuel cells, geothermal power, waste heat recovery systems, and high temperature electronics cooling. Since 2004, we have been conducting life tests at temperatures up to 550 K with water and Commercially Pure Titanium Grade 2 (CP-Ti), titanium alloys, Monel 400, and Monel K500 heat pipes. Since 2006, life tests have been conducted at temperatures up to 673 K with titanium and Hastelloy B-3, C-22, and C-2000 envelopes paired with AlBr3, GaCl3, SnCl4, TiCl4, and TiBr4 halide working fluids. Recently, roughly half of these heat pipes were selected for destructive evaluation. The working fluids were analyzed, and sections of the heat pipes were examined to determine the type and amount of corrosion in the wicks and heat pipes. The results showed that Titanium/water and Monel/water heat pipes are suitable for temperatures up to 550 K. Analysis of titanium/water heat pipe crosssections using optical and electron microscopy revealed little if any corrosion even when observed at high magnifications. Copper depleted zones, as well as copper surface nodules formed on the Monel 400 screen wick, but not on the Monel K500 envelopes. An analysis of the water working fluids showed minimal pickup of metals. The long terms tests also established that Titanium/TiBr4 at 653 K, and Hastelloy B-3, C-22 and C-2000/AlBr3 at 673 K were compatible. Hastelloy C-2000 underwent little corrosion when used with TiCl4 working fluid. Hastelloy C-22 exhibited a 5-10 micrometer thick dual corrosion layer when tested with AlBr3 working fluid. The results indicate that the tested envelope materials and working fluids can form viable material/working fluid combinations.

I. Introduction

There are a number of different applications that could use heat pipes or loop heat pipes (LHPs) in the intermediate temperature range of 450 to 750 K, including space nuclear power system radiators, fuel cells, geothermal power, waste heat recovery systems, and high temperature electronics cooling. The intermediate temperature region is generally defined as the temperature range between 450 and 750 K. At temperatures above 700-725 K, alkali metal (cesium) heat pipes start to become effective. Below about 725 K, the vapor density for cesium is so low that the vapor sonic velocity limits the heat transfer. Historically, water was used at temperatures up to about 425 K. More recently, it has been shown that water can be used with titanium or Monel envelopes at temperatures up to 550 K (Anderson, Dussinger, Bonner, and Sarraf, 2006).

II. Literature Survey

At present, there is no commonly accepted working fluid over the entire intermediate temperature range. Potential working fluids include elemental working fluids such as sulfur, organic compounds, and halides. This paper reviews many of the intermediate temperature heat pipe life tests conducted over the past 40 years, and then recommends suitable working fluid/envelope combinations. Anderson (2006) provides more detailed information on these tests.

A. Elements — Sulfur, S/I, and Mercury

Pure sulfur is not suitable in the intermediate temperature range because of its high liquid viscosity, although it may be useful at higher temperatures. Sulfur has a unique temperature dependent polymerization property at 470 K, which increases its liquid viscosity peak to approximately 100 Pa-s. This is about three orders of magnitude higher than the maximum level for effective heat pipe operation. The addition of a small percentage of iodine reduces the viscosity to a level that may be acceptable for reasonable heat pipe operation (Polasek and Stulc, 1976, Timrot et al., 1981). A potential problem with both sulfur, and sulfur/iodine mixes is that they react strongly with many envelope materials.

There are several problems with mercury as a wetting fluid including:

  • Toxicity
  • Difficulty in achieving good wetting of the wick and wall material without extensive corrosion
  • High density, which translates into increased mass
  • Aggressive attack or solution of many metals, e.g., copper

Additives have been used successfully with mercury to wet coarse, wicks, but it appears to be very difficult to achieve wetting in finer pore wicks. Heat pipe tests with mercury in a sintered stainless steel wick failed because the mercury did not wet the stainless steel (Anderson, Rosenfeld, Angirasa, and Mi, 2004).

Sulfur, Sulfur-Iodine, and Mercury life tests are summarized in Table 1. Mercury is compatible with 347 SS based upon long term life tests. Sulfur is compatible with pure aluminum based on a short term life test, as is Sulfur-10% Iodine with 304 SS.

Table 1. Summary of Sulfur, Sulfur-Iodine, and Mercury Life Tests

B. Organic Fluids

Life tests have been conducted with 19 different organic working fluids. Most of the suitable organic fluids are ring compounds. The reason for this was discussed by Saaski and Owzarski (1977) who pointed out that these types of compounds should be more stable than the long chain hydrocarbons. Saaski and Owzarski also pointed out replacing some (or all) of the hydrogen atoms with fluorine may make the compound more stable.

Potential problems with the organic working fluids include the possibility of polymerization and/or dissociation. Polymerized fluids generally undergo an increase in liquid viscosity, which will decrease the circulation of the working fluid in a heat pipe and therefore its heat transport capacity. Dissociation normally generates noncondensable gases (NCG), which over time will build up in the heat pipe condenser. The presence of NCG reduces the effective length of the heat pipe condenser and hence the area available for heat radiation. This will either cause the temperature to rise at a given power level or the power level to be decreased at a given temperature.

Typically, organic fluids develop problems more quickly as the temperature is increased. The maximum operating temperature for an organic fluid depends both on the operating temperature, and how long the heat pipe needs to operate. For example, Anderson et al. (2007b) tested 304 stainless steel heat pipes with Dowtherm A working fluid. Heat pipes operating at 723 K (450°C) gassed up in ~180 hours, while pipes operating at 673 K (400°C) took roughly 1,500 hours for NCG gas generation to start affecting their behavior.

Table 2. Summary of Diphenyl, Diphenyl Oxide and Eutectic Diphenyl/Diphenyl Oxide Life Tests

Table 3. Summary of Organic Fluid Life Tests Other Than Diphenyl and Diphenyl Oxide

Table 3. (Continued) Summary of Organic Fluid Life Tests Other Than Diphenyl and Diphenyl Oxide

The most commonly tested organic fluids have been diphenyl, diphenyl oxide, and a eutectic mixture of diphenyl/diphenyl oxide (Trade Names Dowtherm A, Therminol, and Diphyl). Eutectic diphenyl/diphenyl oxide is nearly an azeotrope (Basilius and Prager, 1975), so the liquid and vapor have almost the same composition. This avoids the problems encountered with other mixtures such as NaK, where fractional distillation can occur (Anderson, 1993). Life test results for these three fluids are summarized in Table 2.

When using diphenyl, diphenyl oxide, or diphenyl/diphenyl oxide at temperatures over 673 K (400°C), noncondensable gas is generated in a relatively short time periods shown in Table 2. The exact period depends upon the fluid and material and decreases as the temperature increases. For example, Kenney and Feldman found that their diphenyl pipes took less than 72 hours to gas up at 748 K (475°C), and 366 hours to gas up at 695 K (422°C). Between 573 and 673 K (300 and 400°C), these fluids are generally suitable, for short duration tests near 673 K, and long duration tests near 573 K. For example, Groll et al. found that 321 SS was compatible for ~40,000 hours at 573 K (300°C), but not at 623 K (350°C).

Life tests results for organic fluids other than diphenyl and diphenyl oxide are summarized in Table 3. Fluids have been ranked by the highest temperature for a compatible life test with any envelope material.

Since all of their life tests to date have been compatible, two fluids stand out in Table 3: toluene and naphthalene. Toluene was compatible with a copper-nickel alloy, CuNi10Fe, at 553 K (280°C), as well as with aluminum, mild steel, stainless steel, and titanium at lower temperatures. This is probably close to the maximum useful range of toluene, since the critical point of toluene is 592 K (319°C).

Water is generally a better working fluid, since it can also be used in this temperature range, and has a Merit number that is roughly 50 times higher than toluene. However, toluene has three advantages over water, which may make it a suitable choice for certain conditions. The advantages are:

  • Compatibility with a larger number of envelope/wick materials
  • Melting temperature of 178 K (-95°C) versus 273 K (0°C)
  • Lower saturation pressure (e.g., 23.4 atm. at 550 K versus 60.4 atm. for water)

Naphthalene is compatible with stainless steel, copper-nickel, and titanium, based on long term life tests at 593 K (320°C) and above. It has also been shown to be compatible at lower temperatures with aluminum and mild steel. It was compatible with Alloy 20 stainless steel for short term tests at 380°C.

While fluorinated compounds have been theorized to be more stable than the same compound without fluorine, this has not been verified in life tests date. Gryzll, Back, Ramos, and Samad, (1994) found that Decafluorobyphenyl (C12F10) was less stable than Diphenyl (C12H10) under the same test conditions. Perfluoro-1,3,5-triphenylbenzene underwent severe thermal decomposition. Naphthalene was compatible with mild steel at 623 K (350°C) for 5,520 hours, while Monochloronaphthalene was found to be unsuitable after 642 hours at 560 K (287°C), and Octafluoronaphthalene had NCG gas generation at 488 K (215°C). Other stable, fluorinated life tests have been conducted at temperatures of 530 K (257°C) and below.

C. Halides

A halide is a compound of the type MX, where M may be another element or organic compound, and X may be any of the Group 17 elements: fluorine, chlorine, bromine, iodine, or astatine. Starting with Saaski and Owarski (1977), a number of researchers have suggested that halides are potential heat pipe fluids. They are attractive because they are more stable at high temperatures than organic working fluids, and because their Merit number peaks in the intermediate temperature range. Information on halide properties can be found in Anderson, Rosenfeld, Angirasa, and Mi (2004) and Devarakonda and Anderson (2005).

Saaski and Owzarsky (1977) proposed an electrochemical method to predict the compatibility of halide working fluids with envelope materials. Tarau, Sarraf, Locci and Anderson (2007) found that this procedure had good agreement with the halide life tests discussed above.

Halide life tests are summarized in Table 4. Some halides appear to be suitable for temperatures up to 673 K (400°C), and possibly at higher temperatures. Tests are ongoing with TiBr4/titanium at 653K (380°C), and with AlBr3/Superalloys at 673K (400°C). Very long term life tests show that TiCl4 and SnCl4 are both compatible with mild steel. No tests to date with an aluminum envelope have been successful. This is due to the very high decomposition potential of aluminum when compared to other metals (Tarau, 2007).

Table 4. Halide Life Test Summary

III. Experimental Procedure

A. Water Life Tests

Titanium, titanium alloys, Monel 400, and Monel K500 have higher yield strength and lower density than copper. As discussed above, they have been shown to be compatible with water, hence can be used in thinner and lighter weight heat pipes than copper at a given operating temperature and working fluid vapor pressure. Anderson, Dussinger, Bonner, and Sarraf (2006) started a series of life tests with commercially pure (CP) titanium, titanium alloys, Monel 400, and Monel K-500. The life test results are updated below. The materials under test include:

  • Ti CP-2 Heat Pipe, with CP Titanium Screen
  • Monel K500 Heat Pipe, with Monel 400 Screen
  • Ti Grade 5 Cylinder (6% Aluminum, 4% Vanadium), with CP Titanium Screen
  • Ti Grade 7 Cylinder (0.2% Pd), with CP Titanium Screen
  • Ti CP-2 Cylinder, with 21S foil and CP Titanium Screen (21S tubing was not available)
  • Ti Grade 9 cylinder (3% Aluminum, 2.5% Vanadium) with CP Titanium Screen
  • Ti CP-2 Heat Pipe, with Sintered Cylindrical Wick
  • Ti CP-2 Heat Pipe, with Integral Grooves
  • Monel 400 Heat Pipe, with Monel 400 Screen
  • Monel K500 Heat Pipe, with sintered Monel 400 wick
  • Monel 400 Heat Pipe, with sintered Monel 400 wick

The heat pipes with integral titanium grooves are intended for spacecraft thermal control. A typical cross-section is shown in Figure 1. Three integrally grooved heat pipes are currently on life test at NASA Glenn Research Center (Sanzi and Jaworske, 2011).

Figure 1. Titanium heat pipe with interval grooves for spacecraft thermal control

Table 5. Titanium-Water and Titanium-Monel Life Test Pipes — Operating Hours as of May 6, 2013

Table 5 shows the different life test pipes on test. Monel 400 is a solid solution alloy with roughly 63% nickel and 30% copper. It is a single-phase alloy, since the copper and nickel are mutually soluble in all proportions. It can only be hardened by cold working. Monel K500 is a similar nickel-copper alloy, with the addition of small amounts of aluminum and titanium that give greater strength and hardness. The system is age-hardened by heating so that small particles of Ni3(Ti, Al) are precipitated throughout the matrix, increasing the strength of the material. The advantage of Monel K-500 is that the strength can be partially recovered after a wick is sintered inside.

B. Halide Life Tests

A series of halide life tests are ongoing at ACT. The selection criteria were discussed in Anderson et al. (2007). The fluid/envelope combinations tested and the operating conditions are shown in Table 6. The titanium pipes had a 50 x 50 mesh titanium screen wick, and the C-22 pipes had an 80 x 80 mesh C-22 wick. The other two types of pipes were bare. Note that all of the superalloy pipes had C-22 endcaps and fill tubes (due to availability).

The operating temperatures in Table 6 were set based on the vapor pressure, and the allowable stresses in each heat pipe as a function of temperature. During the life tests, the temperature of the evaporator and condenser for each heat pipe are monitored, to detect any problems. It is possible that oxygen can affect the outside of the titanium pipes during the test. To prevent this problem, the life tests are conducted inside a box that is purged with argon. During the life test, heat pipe temperatures are monitored to detect the formation of non-condensable gas.

The superalloy/GaCl3 pipes all leaked at the pinchoff weld after roughly one week of operation at 360°C (633K). Note that all of the superalloy pipes used a C-22 fill tube, since that was more readily available. After roughly 11,000 hours, the Hastelloy B3 pipe with AlBr3, apparently at a weld. Note that this failure is probably due to the pipe being severely overheated after the first 300 hours of testing when the heater shorted out. The maximum temperature is not known, however, it was sufficient to bubble the aluminum heater block. The titanium/GaCl3, titanium/TiBr4, and superalloy/SnCl4 pipes all developed large amounts of non-condensable gas. After roughly 20,000 hours of operation, the pipes were taken off life test, and stored for the analyses discussed below.

One superalloy/TiCl4 and one superalloy/AlBr3 pipe continue to run without any problem (the others were taken down for destructive analysis). These pipes have currently been running for 57,000 hours (6.7 years). The AlBr3 pipes is of particular interest, since it is running at 673 K (400°C). This is close to the temperature at which cesium starts to work.

Table 6. Current Halide Life Test Pipe Temperatures and Operating Times (May 6, 2013)

C. Heat Pipe Sectioning and Analysis

In late 2010, several of the heat pipes were selected for destructive investigation, see Table 6. One of each pair of water life test pipes was selected, while the other one continued on life test. The GaCl3 and SnCl4 pipes were known to be non-compatible, since they generated large amounts of NCG. The heat pipes containing halides were neutralized with water to form a stable sediment. The sediment from the halides, and the water from the heat pipes were collected for chemical analysis. No fluids analysis was done on Pipe 4, CP-Ti/TiBr4, since titanium is the only metal present in the fluid and envelope.

To examine the cross-sections to determine the type and amount of corrosion in the wicks and heat pipes, the heat pipes were cut in half, pressure infiltrated with epoxy and sectioned at a location approximately one-third of the way above the bottom of the heat pipe. The sections were polished through 0.05-micrometer silica and examined using optical and scanning electron (SEM) microscopes.

Table 7. Heat Pipes Selected for Destructive Evaluation

IV. Results and Discussion

A. Examination of Cross-Sections

1. Titanium-Water Heat Pipes

Analysis of the titanium/water heat pipe cross-sections using optical microscopy revealed little if any corrosion when observed at high magnifications. Even using differential interference contrast, it was difficult to find any corrosion layer. When any evidence of corrosion was observed, the layer was typically ~1 micrometer thick. SEM imaging and EDS analysis also did not indicate any substantial corrosion layer.

The Timetal-21S strip placed in Heat Pipe 124 had apparent differences between the surface and the center as shown in Figure 2. On the side that faced the envelope, the layer extends approximately 25 micrometers while on the side facing the center of the heat pipe the layer extends only about 10 micrometers. EDS analysis indicated that there may be depletion of Mo in the layers, but the difference between the center and layers was sufficiently small to be inconclusive.

Heat Pipes 103, 124 and perhaps 122 also had evidence of a layer on the surface of the wires of the wick and envelope. An example is shown in Figure 3. A layer approximately 5 to 10 microns thick that is not mottled like the core can be observed in BSE images. The layer does not have a detectable difference in chemical composition. It is hypothesized that there has been a change in the grains that has reduced the contrast between grains. This is not caused by thermal exposure since the core does not exhibit the same change. Instead, it is most likely caused by the introduction of interstitial atoms of O and H into the Ti at levels too low to detect by EDS.

It was noted in several cases such as shown in Figure 4 that the wires and, in some cases, envelopes had a very rough surface. It was not possible to compare these surfaces to unexposed samples made from the same stock, so it is not clear if the roughness was caused by drawing of the wire and tubing used. There does not appear to be any corrosion product in the crevices observed in the wires, so it is most likely that these are caused by drawing. Additional investigation is required to confirm this.

Figure 2. BSE Image of Timetal 21-S Strip in Heat Pipe 124 Showing Possible Reaction Layer.

Figure 3. BSE Image of CP Ti Mesh Wire Wick in Heat Pipe 124 (Arrow denotes possible reaction layer)

Figure 4. BSE Image of CP Ti Mesh Wire Wick in Heat Pipe 103 Highlighting Surface Roughness Of Wire.

2. Titanium-Halide Heat Pipes

The two titanium halide heat pipes examined had very different responses. Heat Pipe 4, which had CP Ti with a TiBr4 working fluid, had minimal corrosion. Like Heat Pipes 103 and 124, there was evidence of some change at the surface as the BSE images showed the outer 10 micrometers had notably less mottling than the core.

Heat Pipe 10, which had a CP Ti with GaCl3 working fluid, underwent extensive corrosion as seen in Figure 5. Extensive voids and cracking were observed in the corrosion layer. EDS analysis indicated that the corrosion layer was a Ga-29.7 wt.% Ti alloy. Examination of the Ga-Ti phase diagram (National Physical Laboratory, 2012) showed that the composition is similar to the Ga2Ti phase. Immediately adjacent to the Ga2Ti phase on the phase diagram is Ga(l) and Ga3Ti. Given the extensive nature of the voids, particularly on the wires, the Ga(l) and Ga3Ti(s) phases may have been present in these voids. During neutralization of the halide, the Ga(l) and any Ga3Ti particles within it could have been physically removed, leaving behind the voids.

Some of the corrosion layer was observed to crack and chip during polishing. The fracture surfaces were indicative of a brittle failure mode. In combination with the extensive cracking of the corrosion layer, this seems to indicate that the corrosion layer is quite brittle.

Figure 5. BSE Image of Heat Pipe 10 (CP Ti-GaCl3) Showing Ga-Ti Reaction Layer

3. Monel-Water Heat Pipes

Several water working fluid heat pipes made with Monel K500 (Ni-30Cu-2Fe-2.7Al-0.6Ti) envelopes and Monel 400 (Ni-31Cu-2.5Fe-2Mn) wicks were tested at varying times and temperatures. While the heat pipes performed well overall, there were some surprises when the heat pipe cross-sections were examined.

Figure 6 shows an optical micrograph of the envelope and wick for Heat Pipe 136, one of the heat pipes that underwent the most change. Extensive changes, including the formation of a dark subsurface layer and bright nodules, were observed in the Monel 400 wick. While the change was the most extensive for the Monel-Water heat pipes, the morphology was typical of all Monel 400 wire mesh and powder wicks as well. Heat Pipe 134, which has a Monel 400 envelope, shows a similar dark subsurface layer. It is much thinner, on the order of 1 to 8 micrometers thick, and variable in thickness.

The Monel K500 envelope does not show an extensive change. Close examination of the envelope reveals, at most, a thin (5-10 micrometer) corrosion layer. Most likely the layer was an oxide, but it was sufficiently thin to prevent definitive identification through EDS.

Figure 7 shows a detail of one of the Monel 400 wires from Heat Pipe 107 (Monel K500-Monel 400 wickwater). EDS spot analysis was conducted on the surface nodules, the dark subsurface layer and the matrix. The results showed that the surface nodules were essentially pure Cu, the subsurface layer was Cu-depleted, and the matrix even adjacent to the dark layers retained essentially the same composition as the bulk composition of Monel 400. Additional examination of this and other heat pipes with Monel 400 screens indicated that the dark layer could be between 2 wt.% and 23 wt.% Cu compared to 31 wt.% Cu for the bulk alloy.

Examination of the Cu-Ni phase diagram (ASM International, 1992) shows that while Cu and Ni form a solid solution, below about 627 K (354 °C) there is a decomposition of the α phase to α12 phases. This decomposition creates a Cu-rich and a Ni-rich phase. It appears that this is the driving force for the separation of the Cu and Ni that is observed. Apparently the activity gradient was such that the Cu-rich phase preferentially moved through diffusion to the surface. The addition of several alloying elements to Monel K500 appeared to stabilize the α phase and prevent this decomposition. While no large amounts of oxygen were observed, preferential oxidation of the Ni may have also played a role in the development of the observed morphology and phases.

Since both Monel 400 and Monel K500 are extensively used in steam plant operations, the literature was searched to find similar observations. So far, no such reference has been located. The literature search is continuing so that this phenomena can be better understood.

Figure 6. Optical Bright Field Micrograph of Heat Pipe 136 (Monel K500 Envelope, 120 Mesh Monel 400 Wick and Water Working Fluid)

Figure 7. BSE Image of Monel 400 Wire In Heat Pipe 107 (Monel K500-Monel 400 wick-Water).

4. Hastelloy C-Series Superalloy-Halide Heat Pipes

Four corrosion-resistant Hastelloy C-series superalloy heat pipes were examined. Hastelloy C-22 and C-2000 were paired with SnCl4 as a working fluid in Heat Pipes 7 and 8 respectively. Heat Pipe 153 used a Hastelloy C-2000 envelope with a TiCl4 working fluid, and Heat Pipe 157 paired Hastelloy C-22 with AlBr3 as a working fluid.

Heat Pipe 7 exhibited considerable roughening of the surface (Figure 8) and surface cracks/crevices that extended about 20 micrometer into the envelope (Figure 9). As seen in Figure 10, a corrosion layer about 10 micrometers thick was observed on the surface of the envelope. This layer did not appear to be protective as it had extensive voids, but it did appear somewhat adherent.

BSE imaging of the interface revealed the presence of a lighter phase as seen in Figure 11. EDS spot analysis showed that the lighter phase was a Mo-W-Sn phase. It appears that the Sn from the SnCl4 can react with the Mo and W of the Hastelloy C-22 under the heat pipe operating conditions.

Figure 8. Differential Interference Contrast Optical Micrograph of C-22 Envelope In Heat Pipe 7 Showing Roughening and Corrosion Layer (Hastelloy C-22-80 mesh Hastelloy C-22 Wick-SnCl4)

Figure 9. SE Image of C-22 Envelope In Heat Pipe 7 Showing Typical Crevice (Hastelloy C-22-80 mesh Hastelloy C-22 Wick-SnCl4)

Figure 10. SE Image of C-22 Envelope In Heat Pipe 7 (Hastelloy C-22-80 mesh Hastelloy C-22 Wick-SnCl4)

Figure 11. BSE Image of C-22 Envelope In Heat Pipe 7 Showing Presence Of Lighter Mo-W-Sn Phase (Hastelloy C-22-80 mesh Hastelloy C-22 Wick-SnCl4)

The Hastelloy C-2000 envelope of Heat Pipe 8 also underwent extensive reaction with the SnCl4 working fluid. A 200 micrometer thick corrosion layer shown in Figure 12 was observed. The layer showed extensive cracking including cracking at the interface, which indicates it may not be adherent or has a large coefficient of thermal expansion mismatch with the Hastelloy C-2000 substrate. EDS analysis of the corrosion layer revealed that it was primarily Ni and Sn with some Cl. It appears to be Ni3Sn2 modified by reaction or incorporation of about 9 wt.% Cl and minor amounts of Cr, Cu, Fe and Mn from the Hastelloy C-2000. EDS analysis of the matrix immediately beneath the corrosion layer did not indicate any change in the composition from the bulk composition, indicating that there was no depleted zone beneath the corrosion layer.

In addition to the Ni-Sn-Cl corrosion layer, Mo-Cl particles were observed during X-ray mapping. These generally occurred at the interface between the corrosion layer and the substrate. It was not possible to perform an EDS analysis on the particles due to their small size relative to the excitation volume of the SEM beam, but the Xray maps qualitatively indicated that considerably more Cl was present relative to the corrosion layer.

Figure 12. BSE Image of C-2000 Envelope In Heat Pipe 8 Showing Presence Of Thick Ni-Sn-Cl Reaction Layer. (Hastelloy C-2000-SnCl4)

Heat Pipe 153 paired Hastelloy C-2000 with TiCl4 as the working fluid. SEM observations such as the image shown in Figure 13 revealed a 1 to 2 micrometer thick corrosion layer on the surface. The thickness of the layer varied as the outer surface was not planar. EDS analysis showed the reaction layer consisted of Ni-33 wt.% Ti-18 wt.% Mo-18 wt.%Cr-4 wt.% Cu-2 wt.% Cl. The layer, while non-uniform does appear to be somewhat protective and adherent.

High magnification BSE images of the interface such as the one shown in Figure 14 showed the presence of a very thin (~0.5 micrometer) thick layer beneath the reaction layer that was darker than the surrounding matrix. The thinness of the layer prevented good EDS analysis, but the BSE indicates that there is a diffusion zone beneath the reaction layer that has lost the heavier elements such as Mo. This is consistent with the 18 wt.% Mo observed in the reaction layer.

Figure 13. SE Image of C-2000 Envelope In Heat Pipe 153 Showing Presence Of Reaction Layer (Hastelloy C-2000-TiCl4)

Figure 14. SE Image of C-2000 Envelope In Heat Pipe 153 Showing Presence Of Reaction Layer (Hastelloy C-2000-TiCl4)

Heat Pipe 157, which had a Hastelloy C-22 envelope and wick with AlBr3 working fluid, exhibited a dual corrosion layer with a total thickness of 5 to 10 micrometers. The two corrosion layers were about equal in thickness, but there is variability due to a wavy interface between the two layers. EDS analysis of the two layers showed that the outer layer composition was Ni-11.5 wt.% Cr-11.9 wt.% Mo-3.6 wt.% Fe-9.4 wt.% W-0.6 wt.% Mn-1.7 wt.% Co-0.3 wt.% V-0.8 wt.% Si-9.5 wt.% Br. The inner corrosion layer composition was Ni-12.8 wt.% Cr-12.4 wt.% Mo-3.2 wt.% Fe-6.4 wt.% W-0.2 wt.% Mn-1.3 wt.% Co-0.3 wt.% V-21.9 wt.% Br. Spot EDS analysis immediately beneath the corrosion layer showed the presence of 1 wt.% Br, indicating that the Br may be diffusing into the metal substrate. Based upon these analyses, it appears that Br can react with the C-22, but it takes a considerable length of time to build up the corrosion layers., in this case 28,560 hours.

As shown in Figure 15, there is evidence of through-thickness cracking in the inner corrosion layer. This may be caused by a CTE mismatch between this layer and the substrate since there is no continuation of the crack into the outer layer and there is no evidence of any reaction on the surfaces of the cracks or development of corrosion product within the cracks. If this is the case, operating the heat pipes isothermally should result in no cracking and a relatively protective corrosion layer.

Figure 15. SE Image of C-22 Envelope In Heat Pipe 157 Showing Two Corrosion Layers (Hastelloy C-22-AlBr3)

B. Chemical Analysis of Working Fluids

Table 7 contains the results of the chemical analysis of the working fluids. Only the elements that could be present from dissolution of the metals are listed. Since the halides are reactive, they were chemically neutralized with water prior to chemical testing to allow safe testing of the working fluids. The stable sediment was then sent out for analysis.

The chemical analyses of the heat pipes that use water as a working revealed that there was some pickup of metal from the metals, most notably Cu for the Monel heat pipes. However, the levels were in the very low ppm range and represent very minimal contamination of the water. There was no evidence of corrosion that resulted in the movement of metal from the envelopes and wicks to the working fluid. For the Monel samples, this is consistent with the diffusion of Cu to the surface rather than a dissolution/precipitation process for creating the large Cu surface nodules.

The heat pipes that used halides as a working fluid showed more contamination of the working fluids. Heat pipes 153 and 157 which appeared to form a protective corrosion layer showed some of the lowest amounts of contamination. the total contamination was on the order of 300 to 350 ppm. While indicating some corrosion occurred, the amount is small and should be relatively insignificant.

All of the heat pipes with a high gas content showed had 1% or more or the envelope constituents dissolved in the halide. In comparison to Heat Pipes 153 and 157, Heat Pipes 7 and 8 which used SnCl4 suffered considerably more contamination of the working fluids with Cr being the major metal present though traces of most constituents of the alloys used for the envelopes and wicks are observed. The relative amounts seem to be consistent with the levels of attack observed with Heat Pipe 8 undergoing much more attack and reaction than Heat Pipe 7.

Since titanium was the only metal in both the envelope and fluid, No fluid analysis was made for Heat Pipe 4 (CP-Ti/TiBr3), which had little evidence of attack. The high level of Ti in the GaCl3 for Heat Pipe 10 is consistent with the large amount of corrosion and possible Ti-containing particles in the working fluid. Recall that this pipe developed a leak in the first few hours after it was put on life test.

Table 8. Contaminants Found in Working Fluids (weight percent)

V. Conclusion

A survey was conducted for intermediate temperature life tests. Life tests have been conducted with 30 different intermediate temperature working fluids, and over 60 different working fluid/envelope combinations. Life tests have been run with three elemental working fluids: sulfur, sulfur-iodine mixtures, and mercury. Other fluids offer benefits over these three liquids in this temperature range. Mercury is toxic, has a high density, and problems have been observed with getting the mercury to wet the heat pipe wick. Sulfur and Sulfur/Iodine have high viscosities, low thermal conductivities, and are chemically aggressive.

Life tests have been conducted with 19 different organic working fluids. As the temperature is increased, all of the organics start to decompose. Typically they generate non-condensable gas, and often the viscosity increases. At high enough temperatures, carbon deposits can be generated. The maximum operating temperature is a function of how much NCG can be tolerated, and the heat pipe operating lifetime. Three sets of organic fluids stand out as good intermediate temperature fluids:

  1. Diphenyl, Diphenyl Oxide, and Eutectic Diphenyl/Diphenyl Oxide (Dowtherm A, Therminol VP, Diphyl)
  2. Naphthalene
  3. Toluene

A non-organic working fluid is desirable for nuclear fission space power and other applications where radioactivity can generate gas with organic working fluids. Long term life tests show that Superalloys/TiCl44 at 573 K (300°C), and Superalloys/AlBr3 at 673K (400°C) are compatible. As of May 2013, the AlBr3 and TiCl4 tests have been running for over 59,000 hours (6.7 years).

Hastelloy C-2000 underwent little corrosion when used with TiCl4 working fluid, with the formation of only a 1-2 micrometer thick corrosion layer. Hastelloy C-22 exhibited a 5-10 micrometer thick dual corrosion layer when tested with AlBr3 working fluid. The working fluids of these two heat pipes exhibited total metal contents between 300 and 350 ppm. The results indicate that the tested envelope materials and working fluids can form viable material/working fluid combinations.

Titanium/water and Monel/water heat pipes are compatible at temperatures up to 550 K, based on ongoing life tests that have been running for up to 72,000 hours (8.2 years) as of May 2013. Analysis of titanium/water heat pipe cross-sections using optical and electron microscopy revealed little if any corrosion even when observed at high magnifications. When any evidence of corrosion was observed, the layer was typically around 1 micrometer thick. Copper depleted zones, as well as copper surface nodules formed on the Monel 400 screen wick. This was not observed on the Monel K500 envelopes. An analysis of the water working fluids showed minimal pickup of metals.


BSE          Backscatter Electron (Image)
EDS          Energy Dispersive Spectroscopy
SE             Secondary Electron (Image)


The water and halide life tests were sponsored by NASA Glenn Research Center under Contracts NNC05TA36T, and NNC06CA74C. We would like to thank Duane Beach, Cheryl Bowman, Ivan Locci, and Jim Sanzi of NASA Glenn Research Center for helpful discussions about the fluids and materials. We would also like to thank Laurie Anderson, Al Basiulis, Claus Busse, Don Ernst, Manfred Groll, Larry Grzyll, and Bob Reid for their generous help in locating and supplying references. The authors would like to acknowledge the metallographic sample preparation by Joy Buehler of NASA. Any opinions, findings, and conclusions or recommendations expressed in this article are those of the authors and do not necessarily reflect the views of the National Aeronautics and Space Administration.


  1. W. G. Anderson, S. Tamanna, C. Tarau, J. R. Hartenstine, and D. Ellis, “Intermediate Temperature Heat Pipe Life Tests”, 16th International Heat Pipe Conference, Lyon, France, May 20-24, 2012
  2. W. G. Anderson, J. R. Hartenstine, D. B. Sarraf, and C. Tarau, “Intermediate Temperature Fluids for Heat Pipes and Loop Heat Pipes,” 15th International Heat Pipe Conference, Clemson, SC, April 25-30, 2010.
  3. Anderson, W. G., “Intermediate Temperature Fluids for Heat Pipes and LHPs,” W.G. Anderson, Proceedings of the 2007 IECEC, AIAA, St. Louis, MO, June 25-27, 2007a.
  4. Anderson, W.G., Bonner, R.W., Dussinger, P.M., Hartenstine, J.R., Sarraf, D.B., and Locci, I.E., “Intermediate Temperature Fluids Life Tests – Experiments” Proceedings of the 2007 IECEC, AIAA, St. Louis, MO, June 25-27, 2007b.
  5. Anderson, W.G., Dussinger, P.M., Bonner, R.W., and Sarraf, D.B., “High Temperature Titanium-Water and Monel-Water Heat Pipes,” Proceedings of the 2006 IECEC, AIAA, San Diego, CA, June 26-29, 2006a.
  6. Anderson, W.G., Dussinger, P.M., and Sarraf, D.B., “High Temperature Water Heat Pipe Life Tests,” STAIF 2006, pp. 100-107, American Institute of Physics, Melville, New York, 2006b.
  7. Anderson, W.G., “Evaluation of Heat Pipes in the Temperature Range of 450 to 700 K,” STAIF 2005, Albuquerque, NM, February 13-17, 2005.
  8. Anderson, W.G., Rosenfeld, J.R., Angirasa, D., and Mi, Y., “The Evaluation of Heat Pipe Working Fluids In The Temperature Range of 450 to 750 K,” Proceedings, STAIF-2004, pp. 20-27, Albuquerque, NM, February 8-12, 2004.
  9. Anderson, W.G., “Sodium-Potassium (NaK) Heat Pipe,” Heat Pipes and Capillary Pumped Loops, Ed. A Faghri, A. J. Juhasz, and T. Mahefky, ASME HTD, 236, pp. 47-53, 29th National Heat Transfer Conference, Atlanta, Georgia, August 1993.
  10. ASM International, “Cu-Ni Phase Diagram”, ASM Handbook, Vol. 3, Alloy Phase Diagrams, Materials Park, OH, p. 2-173, 1992.
  11. Basiulis, A., and Prager, R. C., “Compatibility and reliability of heat pipe materials,” AIAA-1975-660, 10th AIAA Thermophysics Conference, Denver, Colo., May 27-29, 1975
  12. Basiulis, A., and Fuller, M., “Operating Characteristics and Long Term Capabilities of Organic Fluid Heat Pipes,” AIAA No. 71-408, AIAA 6th Thermophysics Conference, 1971.
  13. Devarakonda, A. and Anderson, W.G., “Thermo-Physical Properties of Intermediate Temperature Heat Pipe Fluids,” STAIF 2005, Albuquerque, NM, February 13-17, 2005. NASA Report NASA/CR—2005-213582, available from the NASA Glenn Technical Reports Server,
  14. Devarakonda, A., and Olminsky, J.E., “An Evaluation of Halides and Other Substances as Potential Heat Pipe Fluids,” Proceedings of the 2004 IECEC, Providence, RI, August 16-19, 2004.
  15. Deverall, J.E., “Mercury as a Heat Pipe Fluid,” ASME Paper 70-HT/Spt-8, American Society of Mechanical Engineers, 1970.
  16. Eastman, Y., personal communication, 2007
  17. Ernst, D.M., personal communication, 2006.
  18. Groll, M., Brost, O., Heine, D., and Spendel, T., “Heat Transfer, Vapor-Liquid Flow Interaction and Materials Compatibility in Two-Phase Thermosyphons,” CEC Contractors Meeting, Heat Exchangers – Heat Recovery, Brussels, June 10, 1982.
  19. Groll, M., Brost, O., and Roesler, S., “Development of High Performance Closed Two-Phase Thermosyphons as Heat Transfer Components for Heat Recovery from Hot Waste Gases,” EG-Status Seminar, Brussels, October, 1987.
  20. Groll, M., “Heat Pipe Research and Development in Western Europe”, Heat Recovery Systems and CHP (Combined Heat & Power), 9(1), pp. 19-66, 1989.
  21. Grzyll, L.R., Ramos, C., and Back, D.D., “Density, Viscosity, and Surface Tension of Liquid Quinoline, Naphthalene, Biphenyl, Decafluorobiphenyl, and 1,2-Diphenylbenzene from 300 to 400°C,” J. Chem. Eng. Data, Vol. 41, pp. 446-450 1996.
  22. Grzyll, L.R., Back, D.D., Ramos, C., and Samad, N.A., “Characterization and Testing of Novel Two-Phase Working Fluids for Spacecraft Thermal Management Systems Operating Between 300°C and 400°C,” Final Report to Phillips Laboratory, Kirtland Air Force Base, No. PL-TR-95-1089, 1995.
  23. Grzyll, L.R., Back, D.D., Ramos, C., and Samad, N.A., “Characterization and Testing of Novel Two-Phase Working Fluids for Spacecraft Thermal Management Systems Operating Between 300°C and 400°C,” Proceedings of the 1st Annual Spacecraft Thermal Control Symposium, Albuquerque, NM 1994.
  24. Grzyll, L.R., “Heat Pipe Working Fluids for Thermal Control of the Sodium/Sulfur Battery,” Proceedings of the 26th Intersociety Energy Conversion Engineering Conference, Vol. 3, pp. 390-394, American Nuclear Society, La Grange, Illinois, 1991.
  25. Hartenstine, J.R., personal communication, 2007.
  26. Heine, D., Groll, M., and Brost, O., “Chemical Compatibility and Thermal Stability of Heat Pipe Working Fluids for the Temperature Range 200 °C to 400 °C,” 8th ChiSA Congress, Prague, September 3-7, 1984.
  27. Jaworskie, D., personal communication, April 5, 2007.
  28. Kenney, D.D., and Feldman, K.T., “Heat Pipe Life Tests at Temperatures up to 400°C,” Proceedings of the 13th Intersociety Energy Conversion Engineering Conference, pp. 1056-1059, San Diego, CA, Aug. 20-25, 1978.
  29. Locci, I.E., Devarakonda, A., Copeland, E.H., and Olminsky, J.K., “Analytical and Experimental Thermo-Chemical Compatibility Study of Potential Heat Pipe Materials,” Proceedings of the 2005 IECEC, San Francisco, CA, August 15-18, 2005.
  30. Los Alamos Scientific Laboratory, “Quarterly Status Report on the Space Electric Power R&D Program for the Period Ending April 30, 1970, Part 1,” Report No. LA-4446-MS, pp., 2-5, May, 1970.
  31. Los Alamos Scientific Laboratory, “Quarterly Status Report on the Space Electric Power R&D Program for the Period Ending January 31, 1968, Part 1,” Report No. LA-3881-MS, pg. 4, February, 1968a.
  32. Los Alamos Scientific Laboratory, “Quarterly Status Report on the Space Electric Power R&D Program for the Period Ending April 30, 1968, Part 1,” Report No. LA-3941-MS, pg. 2, May, 1968b.
  33. Lundberg, L.B., Merrigan, M., Prenger, F.C., and Dunwoody, W., “Sulphur Heat Pipes,” Energy Technology, Los Alamos Scientific Laboratory, LA 8797-PR, October-December 1980, pp. 69-70.
  34. National Physical Laboratory “Calculated Ga-Ti Phase Diagram”, London, UK,, retrieved March 12, 2012
  35. Polasek, F., and Stulc, P., “Heat Pipe for the Temperature Range from 200 to 600°C,” Proc., Second International Heat Pipe Conference, Bologna, Italy, 2, pg. 711, 1976.
  36. Polasek, F., “Heat Pipe Research and Development in East European Countries,” 6th International Heat Pipe Conference (1987), Heat Recovery Systems and CHP, 9(1), pp. 3-17, 1989.
  37. Reid, R.S., Merrigan, M.A., and Sena, J. T., “Review of Liquid Metal Heat Pipe Work at Los Alamos,” 8th Symposium on Space Nuclear Power Systems, Albuquerque, NM, January 6-10, 1991.
  38. Saaski, E.W., and Owzarski, P.C., “Two-Phase Working Fluids for the Temperature Range 50° to 350°C,” Sigma Research, Inc., Final Report, Contract NAS3-20222, NASA Lewis Research Center, June 1977a.
  39. Saaski, E.W., and Tower, L., “Two-Phase working fluids for the temperature range 100-350°C,” American Institute of Aeronautics and Astronautics, 12th Thermophysics Conference, Albuquerque, NM, June 27-29, 1977b.
  40. Saaski, E.W., and Hartl, J.H., “Two-Phase Working Fluids for the Temperature Range 50 to 350°C,” Sigma Research, Inc., Phase II Final Report, Contract NAS3-21202, NASA Lewis Research Center, March, 1980.
  41. Sanzi, J. L., and Jaworske, D. A., “Heat Pipes and Heat Rejection Component Testing at NASA Glenn Research Center,” Nuclear and Emerging Technologies for Space (NETS-2011), Albuquerque, New Mexico, February 7–10, 2011.
  42. Tarau, C., Sarraf, D.B., Locci, I.E., and Anderson, W.G., “Intermediate Temperature Fluids Life Tests – Theory,” Proceedings, STAIF 2007, Albuquerque, NM, February 11-15, 2007.
  43. Timrot, D.L., Serednitskaya, M.A., Medveditskov, A.N., and Traktueva, S.A., “Thermophysical Properties of a SulfurIodine Binary System as Promising Heat Transfer Medium for Heat Pipes,” Journal of Heat Recovery Systems (now Applied Thermal Engineering), Vol. 1(4), pp. 309-314, 1981.
  44. Vasil’ev, L.L., Volokhov, G.M., Gigevich, A.S., and. Rabetskii, M.I, “Heat Pipes Based on Naphthalene,” Journal of Engineering Physics and Thermophysics, Vol. 54, No. 6, pp. 623-626, 1988.


1Chief Engineer, AIAA Member,
2Engineer II, Technology Development
3Lead Engineer, Aerospace Products
4Manager, Aerospace Products, AIAA Member
5Materials Research Engineer, AIAA Member
613CrMo44 is a 1% Cr-1/2% Molybdenum Steel
7Copper Nickel Alloy, resistant to corrosion in seawater
8AlBr3/B3 pipe was severely overheated at 300 hours testing

Have a Question or Project to Discuss?