An ultra-low magnetic field thermal demagnetizer for high-precision paleomagnetism

Abstract

Thermal demagnetization furnaces are widely used paleomagnetic facilities for progressive removal of naturally acquired magnetic remanence or the imparting of well-controlled laboratory magnetization. An ideal thermal demagnetizer should maintain “zero” magnetic field in the sample chamber during thermal treatments. However, magnetic field noises, including the residual magnetic fields of the construction material and the induced fields caused by the alternating current (AC) in the heating element are always present, which can contaminate the paleomagnetic results at the elevated temperatures or especially for the magnetically weak samples. Here, we designed a new structure of heating wire named “straight core solenoid” to develop a new demagnetization furnace with ultra-low magnetic field noise. Simulation and practical measurements show that the heating current magnetic field can be greatly reduced by using the new technology. Thermal demagnetization experiments demonstrate that the new demagnetizer can yield low noise results even for weakly magnetic samples.

Introduction

Paleomagnetism investigates changes in the geomagnetic field through geologic time by the measurement of natural remanent magnetizations (NRM) recorded by magnetic minerals in natural materials. NRM of geological materials usually consists of multiple components. Therefore, to define the stable characteristic remanent magnetization (ChRM) of geological interests, the secondary remanent magnetization needs be removed using sequential demagnetization techniques (e.g., the stepwise progressive thermal or alternating field demagnetization) (Irving et al. 1961; Schmidt 1993). During thermal demagnetization, specimens are heated to a pre-selected temperature, held for a period of time (e.g., 10–30 min), and then cooled down to the room temperature in “zero” magnetic field environment (Collinson 1983). This treatment will be conducted repeatedly in a stepwise manner till the ChRM is isolated (Thellier 1966; Collinson 1975). Thermal demagnetization is one of the standard demagnetization methods, and thus thermal demagnetization furnaces (or thermal demagnetizers) have been widely equipped in nearly all paleomagnetic laboratories.

Although widely used, the experimental success rate of thermal demagnetization can be relatively low especially for weakly magnetic samples such as sedimentary rocks. It is often found that remanent direction of some specimens become seriously distorted at high temperatures, but the ChRM can still be obtained by alternating field demagnetization using sister specimens (e.g., Holm and Verosub 1988). The failure of thermal demagnetization could be attributed to irreversible thermal physio-chemical alterations upon heating (e.g., Wasilewski 1969; Heller et al. 1970), partial thermoremanent magnetization (pTRM) acquisition in the presence of a residual DC field upon cooling (Collinson 1975), or magnetic fields caused by the heating current (Heller et al. 1970). Although early studies did not detect differences between inductive and non-inductive heating wire (Irving et al. 1961), inductive alternating fields (AF) can cause unwanted AF demagnetization behavior at high temperatures. Given that the coercivity of magnetic minerals reduces quickly as the temperature approaches the unblocking temperature or Curie temperature, this effect may be substantial. In the extreme, the NRM direction could be biased by single axis AF demagnetization because of the stationary current field (Stephenson 1983) at high temperature.

Reducing the residual fields in thermal demagnetizers can significantly improve the quality of paleomagnetic measurements, particularly for weakly magnetized specimens. Moreover, for the study of meteorites in planetary science or magnetizations acquired near the onset of the geodynamo, understanding the characteristic remanent magnetization acquired in low magnetic fields, including extremely weak fields (nT range) is a topic of great interest (Weiss et al. 2010; Tarduno et al. 2015; Wang et al. 2017). It is important that the technology around thermal demagnetizers progress to keep pace with the changing demands of the scientific community.

In this study, we will first describe the technology to reduce the residual magnetic field for a newly designed thermal demagnetizer. The key point is to reduce the current magnetic field by adopting a new structure of heating element. We then conduct thermal demagnetization experiments to test the performance of the new furnace.

Newly designed furnace for thermal demagnetization

The heating elements in thermal demagnetizers are typically constructed of non-inductive windings in order to minimize the AC demagnetization effect of the heating current (Chamalaun and Porath 1968). There are generally two types of non-inductive heater winding, one is a bifilar solenoid wrapped on a cylindrical form to heat specimens within (Fig. 1a). This style of winding is widely used in small furnaces such as the Sogo Fine-TD furnace in Japan (Zheng et al. 2010a, b). It is also used in some Kappabridges and variable field translation balances (VFTBs) to heat specimens. In this configuration, the opposing currents of adjacent wires reduce the AC magnetic field. In addition, the wire spacing should be small enough to efficiently reduce the residual magnetic field. A disadvantage of this system, however, is that it will increase the risk of short circuit, and often lead to limited sample capacity in order to maintain an acceptable resistance and workable power consumption.

Fig. 1

Configuration of non-inductive heating wires. a Bifilar solenoid wrapped for a small oven, b solenoid-like helical heating wires arranged in a larger oven, c the new straight core solenoid heating wires using in the TD-PGL-100. Arrows indicate the current flow direction

An alternative method is to use solenoids arranged in opposite direction (Fig. 1b) or wound into a helix as in many commercial furnaces. It is usually assumed that the magnetic field generated by a uniform solenoid is only in the interior and both ends of the solenoid, but this neglects the fact that for a real solenoid the wire loops (and current loops) are not perfectly circular, the current must go from one end to the other, which results in non-zero external fields. Therefore, it is necessary to consider the magnetic field distribution outside a helical solenoid.

Simulated calculation of solenoid magnetic field

The magnetic field distribution outside a solenoid can be calculated using the Biot–Savart law (Hagel et al. 1994; Budnik and Machczynski 2011). Assuming a current, I, flowing in a finite solenoid with a radius of R and a pitch of p, the vectors of magnetic field at point P (Fig. 2) produce by a differential current element Idl at source point N(Xs, Ys, Zs) can be written as:

$$ dB = \frac{{\mu_{0} I}}{4\pi }\frac{{d\mathop{l}\limits^{\rightharpoonup} \times \mathop{r}\limits^{\rightharpoonup} }}{{r^{3} }}, $$

(1)

Fig. 2

Schematic diagram for calculating magnetic field outside of solenoid (R is the radius of solenoid, p = 2πa is the pitch distance and d is the distance between point P and central axis of solenoid)

where r is distance from the point N on the filament to the field point P. Xs = RcosƟ, Ys = RsinƟ and Zs = aƟ since the point N is on the solenoid, where a is the pitch factor.

From cylindrical coordinates to Cartesian coordinates, dl and r can be expressed as:

$$ d\mathop{l}\limits^{\rightharpoonup} = \mathop{i}\limits^{\rightharpoonup} dx + \mathop{j}\limits^{\rightharpoonup} dy + \mathop{k}\limits^{\rightharpoonup} dz = - \mathop{i}\limits^{\rightharpoonup} R\sin \theta d\theta + \mathop{j}\limits^{\rightharpoonup} R\cos \theta d\theta + \mathop{k}\limits^{\rightharpoonup} ad\theta , $$

(2)

$$ \mathop{r}\limits^{\rightharpoonup} = \mathop{i}\limits^{\rightharpoonup} (x_{0} - R\cos \theta ) + \mathop{j}\limits^{\rightharpoonup} (y_{0} - R\sin \theta ) + \mathop{k}\limits^{\rightharpoonup} (z_{0} - a\theta ). $$

(3)

Therefore:

$$ d\mathop{l}\limits^{\rightharpoonup} \times \mathop{r}\limits^{\rightharpoonup} = \left| {\begin{array}{*{20}c} {\mathop{i}\limits^{\rightharpoonup} } & {\mathop{j}\limits^{\rightharpoonup} } & {\mathop{k}\limits^{\rightharpoonup} } \\ { - R\sin \theta d\theta } & {R\cos \theta d\theta } & {ad\theta } \\ {x_{0} - R\cos \theta } & {y_{0} - R\sin \theta } & {z_{0} - a\theta } \\ \end{array} } \right|, $$

(4)

and we have

$$ dB_{x} = \frac{{\mu_{0} I}}{4\pi }\frac{{\left[ {(z_{0} - a\theta )R\cos \theta - (y_{0} - R\sin \theta )a} \right]d\theta }}{{\left[ {(x_{0} - R\cos \theta )^{2} + (y_{0} - R\sin \theta )^{2} + (z_{0} - a\theta )^{2} } \right]^{{{\raise0.7ex\hbox{$3$} \!\mathord{\left/ {\vphantom {3 2}}\right.\kern-\nulldelimiterspace} \!\lower0.7ex\hbox{$2$}}}} }}, $$

(5)

$$ dB_{y} = \frac{{\mu_{0} I}}{4\pi }\frac{{\left[ {(z_{0} - a\theta )R\sin \theta + (x_{0} - R\cos \theta )a} \right]d\theta }}{{\left[ {(x_{0} - R\cos \theta )^{2} + (y_{0} - R\sin \theta )^{2} + (z_{0} - a\theta )^{2} } \right]^{{{\raise0.7ex\hbox{$3$} \!\mathord{\left/ {\vphantom {3 2}}\right.\kern-\nulldelimiterspace} \!\lower0.7ex\hbox{$2$}}}} }}, $$

(6)

$$ dB_{z} = - \frac{{\mu_{0} I}}{4\pi }\frac{{\left[ {(y_{0} - R\sin \theta )R\sin \theta + (x_{0} - R\cos \theta )R\cos \theta } \right]d\theta }}{{\left[ {(x_{0} - R\cos \theta )^{2} + (y_{0} - R\sin \theta )^{2} + (z_{0} - a\theta )^{2} } \right]^{{{\raise0.7ex\hbox{$3$} \!\mathord{\left/ {\vphantom {3 2}}\right.\kern-\nulldelimiterspace} \!\lower0.7ex\hbox{$2$}}}} }}. $$

(7)

As the radius of the solenoid decreases, or when the distance between the point P and solenoid is much larger than the radius, R can be approximately ignored. The point N on a straight wire is $(0,0,a\theta )$, and filament became as $d\mathop{l}\limits^{\rightharpoonup} = \mathop{k}\limits^{\rightharpoonup} ad\theta$, and $\mathop{r}\limits^{\rightharpoonup} = \mathop{i}\limits^{\rightharpoonup} x_{0} + \mathop{j}\limits^{\rightharpoonup} y_{0} + \mathop{k}\limits^{\rightharpoonup} (z_{0} - a\theta )$, and therefore, the formula of magnetic field can be simplified as:

$$ dB_{x} = - \frac{{\mu_{0} I}}{4\pi }\frac{{y_{0} ad\theta }}{{\left[ {x_{0}^{2} + y_{0}^{2} + (z_{0} - a\theta )^{2} } \right]^{{{\raise0.7ex\hbox{$3$} \!\mathord{\left/ {\vphantom {3 2}}\right.\kern-\nulldelimiterspace} \!\lower0.7ex\hbox{$2$}}}} }}, $$

(8)

$$ dB_{y} = \frac{{\mu_{0} I}}{4\pi }\frac{{x_{0} ad\theta }}{{\left[ {x_{0}^{2} + y_{0}^{2} + (z_{0} - a\theta )^{2} } \right]^{{{\raise0.7ex\hbox{$3$} \!\mathord{\left/ {\vphantom {3 2}}\right.\kern-\nulldelimiterspace} \!\lower0.7ex\hbox{$2$}}}} }}, $$

(9)

$$ dB_{z} = 0. $$

(10)

It can be seen that when the solenoid diameter is small, the magnetic field generated by the solenoid is roughly the same as that of a straight wire. Therefore, to reduce the stray external fields of a solenoid, a straight wire can be inserted through its core and connected with solenoid at one end, such that the current in the straight wire is flowing opposite to the current in the solenoid (Fig. 1c). A new heating element is designed based on this configuration which we call it straight core solenoid, and will be used to manufacture our new thermal demagnetizer.

To simulate a heating element solenoid, we assume that the solenoid length is 1 m, the radius is 4 mm, and the pitch is also 4 mm. And the current is set to 1 A. We simulate the fields in YZ plane (Fig. 2) along the direction of solenoid axis, at a distance of 20 mm and 10 mm from central axis. The results are shown in Fig. 3. Only absolute values of field are shown in Fig. 3a because of the logarithmic scale. It is found that the perpendicular component (X) is higher than the radial component (Y) and parallel components (Z), and the X component can be reduced by two orders of magnitude if a straight wire with reverse current is passed through the center of the solenoid. The Y and Z components remain unchanged, since the magnetic field produced by the straight wire wraps around the wire, which is shown here in the X direction only. The fluctuations of field value were also observed at very close to the solenoid and the period is consistent with the pitch (Fig. 3b). As the distance increases, the periodic fluctuation becomes insignificant (Hagel et al. 1994). The magnetic field distribution in other cases can be obtained by changing parameters of the solenoid, such as radius, pitch. It is useful to optimize the structure of heating wire before practical manufacture.

Fig. 3

Magnetic field simulations of single long solenoid at a 10 mm and b 20 mm from the central axis. The black symbol represents the result of conventional solenoid and the red symbol represents the result of a solenoid with a reverse straight wire at solenoid axis. Insets in b show detail measurements over the central 50-cm highlighting period nature of the field, which is caused by the solenoid pitch

In fact, the whole heater group consists of a series of parallel or anti-parallel heating element solenoid and its configuration determined the magnetic field inside the furnace. We calculate the magnetic field distribution in the furnace. The heater composed of 12 conventional solenoids or new heating elements with opposite current direction between adjacent is simulated. Contour maps of different components are shown in Fig. 4. The parameters of each solenoid are the same as those used in Fig. 3, and the current is still set to 1 A. X, Y and Z represent the magnetic field in horizontal, vertical and along the axis direction in the furnace, respectively. It can be seen that the magnetic field in the center of the furnace is extremely low for both configurations, but the low magnetic field area is considerably enlarged in the furnace with new heating elements. The magnetic field inside the solenoid is relatively complex, but does not affect the thermal demagnetization samples. Different configurations which are consistent with some practical applications can also be simulated. A large magnetic field may be produced by parallel connection of heating wire groups (Fig. 5). However, the magnetic field is still very low inside the furnace with same configuration using the new straight core solenoid.

Fig. 4

Contour map of magnetic field distribution on different components in middle cross section of the furnace with composed of 12 conventional solenoids (a–c) and new heating elements (d, e). f The position of the solenoids and the corresponding current direction in adjacent. Letter X, Y, Z in the middle of the graph represents the direction of the magnetic field

Fig. 5

Contour map of magnetic field distribution if the solenoids are wired such that the current flow is parallel. a–c The field distribution composed of 12 conventional solenoids, and d, e the field distribution with new heating elements. f The position of the solenoids and the corresponding current direction in adjacent. Letter X, Y, Z in the middle of the graph represents the direction of the magnetic field

Measurement of solenoid magnetic field

In order to verify the effectiveness and determine the magnetic field of the new heating element, the respective magnetic fields produced by the conventional solenoid heating wire and the new heating element were measured with a triaxial fluxgate magnetometer (APS520). One solenoid heating element with length of 1 m and diameter of 8 mm was placed inside a magnetically shielding cylinder with 1 A DC current applied in the wire (Fig. 6a). The fluxgate sensor was placed to the side of solenoid at vertical distance of about 20 mm and moved along the long axis direction. The magnetic field at different positions was observed with the current on then off. In the same way, we measured the magnetic field of our new straight core solenoid heating element, which is composed of the same solenoid with a straight wire passing through it (Fig. 6b). The solenoid and the straight wire were isolated by a ceramic sheath. The results are shown in Fig. 6c. The magnetic field of conventional solenoid is about 6000–7000 nT and field direction is almost perpendicular to the long axis of solenoid and is consistent with the simulation, which is almost equivalent to that of an axial line current. The stray magnetic field of the straight core solenoid is much lower than the standard solenoid, with a total field intensity of 26–535 nT.

Fig. 6

Magnetic field measurement of conventional solenoid a and new heating wire b. c Current field at different positions, the black line represents the result of conventional solenoid and the red dash line represents the result of a straight core solenoid. The length of solenoid is 1 m, the radius is 4 mm and with pitch distance of 4 mm. The DC current of 1 A applied in the wire during measurement

In our prototype, thermal demagnetizer adjacent elements are arranged in opposite directions (Fig. 7a). The magnetic field at different positions along the axis of the heating chamber were measured when a DC current of 1 A is applied to the heating wire. We measured the magnetic field four times at different vertical distances from the center axis. The peak magnetic field in the sample region is about 130 nT (Fig. 7b). In order to verify the effect, we also arranged the conventional solenoids following the same structure, and the current of adjacent solenoids is opposite. It is found that the magnetic field in the center is relatively low (115–285 nT in sample zone), but gradually increases toward the edge of the furnace (Fig. 7c). However, if the wire connection is changed, parallel connection of two groups are adopted, the magnetic field will become higher and mainly in the vertical direction (Fig. 7d). The measured results are consistent with the numerical simulation.

Fig. 7

a Photo of the new furnace chamber. b Current field (red triangles) with 1 A applied to the heating wire along longitude axis in the newly designed furnace (multiple curves represent different vertical distances from the central axis). c Current field with 1 A applied to the heating wire along longitude axis in conventional furnace, the current of adjacent solenoids is opposite. d Current field with 1 A applied to the heating wire along longitude axis in conventional furnace, currents of adjacent solenoids in each group are opposite, but two groups in parallel connect

Degaussing the shield cylinder and the TD-PGL-100

In order to shield the influence of external magnetic field, the chamber of thermal demagnetization furnace is usually installed in a cylindrical magnetic shield cylinder. The residual fields in sample zone typically vary from several nT to 150 nT in different furnaces (Paterson et al. 2012), which is mainly determined by the remanent magnetization of magnetic materials within the furnace, especially the shields (Freake and Thorp 1971; Thiel et al. 2007). A lower residual field can be achieved by AF demagnetization of the shield cylinder. Early experiments found that the best shield demagnetization results were obtained by passing the AC current through conductors within the shield cylinders or by passing the current longitudinally through the shielding material itself (Herrmannsfeldt and Salsburg 1964). A circular magnetic field perpendicular to the central longitudinal axis will be produced in the cylindrical shield if a current conducting straight wire is passed though the longitudinal center axis of the shield cylinder, however, this requires a large current to reach peak demagnetization. In practice, we use a total of eight 4 mm² copper lines wound from inside to outside of the shield cylinder to form a large coil (Fig. 8a), and connected to a transformer with a twisted-pair cable. The transformer has separated primary and secondary windings which can be pulled apart. Separating the windings will generate a nonlinear attenuation of the alternating current in the coil which performs AF demagnetization of the shield cylinder. The residual magnetic field in the sample region can be as low as 1 nT (Fig. 8b), which makes it possible to further reduce spurious fields during thermal demagnetization.

Fig. 8

a Toroidal degaussing coil embodying the shield cylinder. b Residual fields (black circles) along longitude axis in the newly designed furnace

A new furnace named TD-PGL-100 had been built based on above-mentioned techniques. The furnace has a chamber of 120 cm length and 9 cm diameter, and the sample zone is designed as 60 cm in length, which allows up to 100 standard paleomagnetic specimens be treated together. Temperature gradient in the sample zone is within 10 °C of target temperature below 600 °C and 12 °C at 700 °C. The maximum power consumption of the furnace is 4.0 KVA. Employing an adjustable voltage silicon-controlled rectifier over a solid-state relay allows the output power to be decreased as the temperature approaches the target point, which helps to avoid temperature overshoots. With careful tuning, the oven temperature has a 1 °C accuracy with a resolution of 0.1 °C. As the examples of heating and cooling curves shown in Fig. 9, the temperature rises rapidly at the beginning of heating, and gradually approaches the target temperature after ~ 30 min and then the temperature is maintained for a hold time to ensure the samples are thoroughly heated. The cooling fan can be turned on manually or automatically to cool the samples down. The temperature drops rapidly and slows when approaching room temperature. The heating and cooling data can be logged into USB memory automatically, which is essential for the thermal treatment and related experiments particularly for absolute paleointensity studies, where temperature reproducibility is important.

Fig. 9

Temperature curves during heating and cooling at different target temperatures in a thermal demagnetization experiment

Examples of thermal demagnetization experiment

In order to verify the effectiveness of the new furnace, thermal demagnetization experiments were carried out on 12 natural specimens and 8 synthetic specimens using TD-PGL-100. Nine sandstone specimens denoted as “B” were collected from Cenozoic strata in Yunnan, and three muddy limestone specimens denoted as “CM” were from Tibet. The main magnetic carrier mineral of sandstone specimen is hematite (Li et al. 2017). They have only a single univectorial component decaying steadily toward high temperature. The muddy limestone specimens also contain hematite and have multi-component characteristics of different temperature ranges. Hematite specimens synthesized in the lab were chosen to avoid potential thermochemical changes during multiple heatings. The particles of hematite are cubic (Ozaki et al. 1986; Sugimoto et al. 1993) and with a broadly uniform size distribution with an average length and width of 570 nm and 545 nm, respectively.

We have also tried to evaluate the influence of the background magnetic field. After progressive thermal demagnetization of TRM was carried out to identify the unblocking temperature spectrum of the synthetic hematite specimens, the specimens were heated to 700 °C for complete thermal demagnetization, then the progressive thermal demagnetization was repeated. Remanent directions and moments were measured with a cryogenic magnetometer system (2G Enterprises 755) installed in the magnetically shielded room with residual field < 300 nT at IGGCAS. Background noise is typically lower than 2 × 10⁻¹² Am², and the background moment of the sample tray was kept less than 5 × 10⁻¹¹ Am² during the measurements. All the experiments were completed in the paleomagnetic laboratory at the Institute of Geology and Geophysics, Chinese Academy of Sciences (IGGCAS).

The thermal demagnetization experiments of natural specimens show that good demagnetization results can be obtained using the new furnace. The representative experimental results are shown in Fig. 10. The remanence directions of some specimens do not change much after demagnetization at high temperature, when the remanence intensity is less than 10% of the NRM intensity. The ChRM of high temperature can be successfully isolated for the specimens with multi-component characteristics. The magnetic moments of synthetic specimens during the repeated progressive thermal demagnetization are about 0.02–0.05% of the 30 µT TRM (see detail in Additional file 1)). It confirms that the influence by undesirable magnetic fields from the furnace is very small.

Fig. 10

Thermal decay curves and corresponding orthogonal plots of progressive thermal demagnetization of natural specimens. Solid (open) circles indicate projection on the horizontal (vertical) plane

Discussion

For comparison, Zheng et al. (2010a) investigated similar 1-A current field (~ 240 nT) for the commercially available Sogo Fine-TD. They also reported a 0.5-A current field for the ASC TD48 and Natsuhara as being 3600 and 1600 nT, respectively (equivalent to 1 A fields of 7200 and 3200 nT, respectively). We noticed that they obtained an abnormal field higher than 100 µT at 0.3 A in the MMTD80 thermal demagnetizer, which may be produced by the applied field coil for the paleointensity experiment. Subsequently, a low field (48.4nT/A along the oven axis and less than 3nT/A at right angles in oven axis) was reported by Shaw (2010), and a relatively higher field of ~ 840 nT/A by Zheng et al. (2010b), respectively. Our simulation and experimental results show that the magnetic field inside the furnace using conventional solenoid is non-uniform. Although the heater configuration with conventional solenoids can also cancel out the magnetic field especially at the center, for effective cancellation of the fields generated in each solenoid, this design requires that opposing solenoids are perfectly antiparallel. Imperfect alignment results in small, but potentially significant AC fields when large currents are applied during heating (Zheng et al. 2010a, b; Shaw 2010). In contrast, the new design with straight core solenoid can reduce the dependence on symmetry of configuration, and can also obtain a large space of low magnetic field.

We use our new straight core solenoid heating element to build a new furnace named TD-PGL-100. Subsequently measurements in our later builds have peak current field of only ~ 95 nT/A. This new design, which holds up to 100 specimens, represents a 2–3 times reduction in AC fields compared to the eight-specimen Sogo Fine-TD, and a 9 to 77 times reductions compared to other high-capacity demagnetizers. Yuan et al. (2020) investigated paleomagnetic behavior of red beds in the Sangdanlin section using the new furnace. The results can be reasonably compared with the previously published paleomagnetic results for the same section using the ASC TD48 by Yang et al. (2019). Clearly, excellent paleomagnetic directional data of high-temperature component (650–680 °C) can be defined using the data from new furnace, while some remanence directions become erratic after thermal demagnetization at 620–660 °C using the ASC TD48. This comparison supports that the new thermal demagnetizing furnace has better performance.

It should be noted that the current field is an alternating magnetic field. In thermal demagnetization, the current field is more like the effect of AF demagnetization, and the way to cut off the heating current (e.g., abrupt on–off, or gradual ramping, etc.) may affect the demagnetization effect. However, the new design combined with the appropriate mode of AC supply has the potential to further lower the impact. Although our improved heating element can greatly reduce the AC current field, it cannot completely eliminate it. If lower AC magnetic fields are required, the only alternative would be to heat the specimens outside of the primary electrical heating element region. This could be achieved by heating the sample region by hot gas flow heated outside the sample region. This style of furnace can reduce AC current field to practically zero (Heller et al. 1970). Such gas flow furnace systems, however, are limited to heating only a small number of specimens. Our new TD-PGL-100 thermal demagnetizer with lower AC current field and super low residual magnetic fields is a reasonable choice for most paleomagnetic laboratories.

Conclusions

Here, we introduce a new heating element that is composed of a straight wire inserted into solenoid and connected in series at one end, a configuration we call a straight core solenoid. Such a configuration can drastically reduce the stray magnetic fields generated when a current is applied to the heating element. We also adopted a demagnetization procedure that can reduce the residual magnetic field in shield cylinder to less than 1 nT in sample zone. The TD-PGL-100 built with those technologies allows the successful recovery of weak magnetizations blocked at high temperatures and has applications in recovering sedimentary magnetizations, records of geomagnetic polarity reversals, signals of the earliest geodynamo, as well as extraterrestrial magnetizations. One of this new thermal demagnetizers has been running normally for 3 years in the IGCCAS laboratory, and results demonstrate its excellent performance especially for these weakly magnetic natural specimens (Jiang et al. 2017; Yan et al. 2018).